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Characterization and Modelling of Composites, Volume III

A special issue of Journal of Composites Science (ISSN 2504-477X). This special issue belongs to the section "Composites Modelling and Characterization".

Deadline for manuscript submissions: closed (31 July 2023) | Viewed by 115500

Special Issue Editor


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Guest Editor
General Department, Evripus Campus, National and Kapodistrian University of Athens, Psachna, Evoia, Greece
Interests: nanostructures; nanocomposites; composite structures; finite element method; design; modeling; computational analysis; nanotechnology
Special Issues, Collections and Topics in MDPI journals

Special Issue Information

Dear Colleagues,

Composites have been increasingly used in various structural components in the aerospace, marine, automotive, and wind energy sectors. Composites’ material characterization is a vital part of the product development and production process. Physical, mechanical, and chemical characterization helps developers to further their understanding of products and materials, thus ensuring quality control. Achieving an in-depth understanding and consequent improvement of the general performance of these materials, however, still requires complex material modeling and simulation tools, which are often multiscale and encompass multiphysics.

This Special Issue is aimed at soliciting promising, recent developments in composite modeling, simulation, and characterization, in both design and manufacturing areas, including experimental as well as industrial-scale case studies. All submitted manuscripts will undergo a rigorous review and will only be considered for publication if they meet journal standards. 

Dr. Stelios K. Georgantzinos
Guest Editor

Manuscript Submission Information

Manuscripts should be submitted online at www.mdpi.com by registering and logging in to this website. Once you are registered, click here to go to the submission form. Manuscripts can be submitted until the deadline. All submissions that pass pre-check are peer-reviewed. Accepted papers will be published continuously in the journal (as soon as accepted) and will be listed together on the special issue website. Research articles, review articles as well as short communications are invited. For planned papers, a title and short abstract (about 100 words) can be sent to the Editorial Office for announcement on this website.

Submitted manuscripts should not have been published previously, nor be under consideration for publication elsewhere (except conference proceedings papers). All manuscripts are thoroughly refereed through a single-blind peer-review process. A guide for authors and other relevant information for submission of manuscripts is available on the Instructions for Authors page. Journal of Composites Science is an international peer-reviewed open access monthly journal published by MDPI.

Please visit the Instructions for Authors page before submitting a manuscript. The Article Processing Charge (APC) for publication in this open access journal is 1800 CHF (Swiss Francs). Submitted papers should be well formatted and use good English. Authors may use MDPI's English editing service prior to publication or during author revisions.

Keywords

  • fiber-reinforced composites
  • unidirectional and woven reinforcements
  • noncrimp fabrics (NCFs)
  • three-dimensional composites
  • nanocomposites
  • natural fiber and biocomposites
  • hybrid composites
  • composite structures
  • modeling and characterization
  • numerical simulation
  • experimental studies
  • industrial case studies

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Published Papers (58 papers)

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Editorial

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10 pages, 256 KiB  
Editorial
Characterization and Modelling of Composites, Volume III
by Stelios K. Georgantzinos
J. Compos. Sci. 2023, 7(11), 446; https://doi.org/10.3390/jcs7110446 - 27 Oct 2023
Cited by 1 | Viewed by 2189
Abstract
The realm of composite materials continues to evolve, with researchers pushing the boundaries of understanding and application. This Special Issue published in the Journal of Composites Science encapsulates the essence of these advancements, presenting a curated collection of research articles that highlight the [...] Read more.
The realm of composite materials continues to evolve, with researchers pushing the boundaries of understanding and application. This Special Issue published in the Journal of Composites Science encapsulates the essence of these advancements, presenting a curated collection of research articles that highlight the latest developments in the characterization and modelling of composites. The diversity of the covered topics ranges from a foundational understanding of composite behaviours to the application of cutting-edge modelling techniques. Each contribution offers a fresh perspective, expanding our knowledge of composites and setting the stage for future explorations in this dynamic domain. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)

Research

Jump to: Editorial, Review

16 pages, 8305 KiB  
Article
Preliminary Experimental and Numerical Study of the Tensile Behavior of a Composite Based on Sycamore Bark Fibers
by Helena Khoury Moussa, Philippe Lestriez, He Thong Bui, Pham The Nhan Nguyen, Philippe Michaud, Romain Lucas-Roper, Guy Antou, Viet Dung Luong, Pham Tuong Minh Duong, Fazilay Abbès and Boussad Abbès
J. Compos. Sci. 2024, 8(9), 333; https://doi.org/10.3390/jcs8090333 - 23 Aug 2024
Viewed by 897
Abstract
In the context of global sustainable development, using natural fibers as reinforcement for composites have become increasingly attractive due to their lightweight, abundant availability, renewability, and comparable specific properties to conventional fibers. This paper investigates the tensile properties of a sycamore bark fiber-reinforced [...] Read more.
In the context of global sustainable development, using natural fibers as reinforcement for composites have become increasingly attractive due to their lightweight, abundant availability, renewability, and comparable specific properties to conventional fibers. This paper investigates the tensile properties of a sycamore bark fiber-reinforced composite. The tensile tests using digital image correlation showed that, by adding 18% by volume of sycamore bark for the polyester matrix, the tensile modulus achieves 4788.4 ± 940.1 MPa. Moreover, the tensile strength of the polyester resin increased by approximately 90% when reinforced with sycamore bark fiber, achieving a tensile strength of 64.5 ± 13.4 MPa. These mechanical properties are determined by the way loads are transferred between the polyester matrix and fibers and by the strength of the bond between the fiber-matrix interfaces. Since it is difficult and time consuming to characterize the mechanical properties of natural fibers, an alternative approach was proposed in this study. The method consists of the identification of the fiber elastic modulus using a finite element analysis approach, based on tensile tests conducted on the sycamore bark fiber-reinforced composites. The model correctly describes the overall composite behavior, a good agreement is found between the experimental, and the finite element predicted stress–strain curves. The identified sycamore bark fiber elastic modulus is 17,763 ± 6051 MPa. These results show that sycamore bark fibers can be used as reinforcements to produce composite materials. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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Figure 1

Figure 1
<p>Sycamore bark fiber tissue-like structure.</p>
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<p>Extraction process of sycamore bark fibers, from the plant to the fibers.</p>
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<p>Sycamore bark fiber-reinforced composite plate before cutting.</p>
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<p>Composite sample coated with stochastic black and white contrast patterns.</p>
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<p>Cross-section area measurement using ImageJ.</p>
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<p>Geometry model of the composite test specimen.</p>
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<p>Boundary conditions and finite element meshes.</p>
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<p>Mesh sensitivity analysis.</p>
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<p>Experimental stress–strain curves.</p>
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<p>Strain distribution at five different loading stages and corresponding stress vs. strain curve for composite.</p>
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<p>Comparison of mechanical properties of resin and composite.</p>
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<p>SEM micrographs of the sycamore bark fibers bundle at different magnifications: (<b>a</b>) 50×, (<b>b</b>) 150×, (<b>c</b>) 300× and (<b>d</b>) 2000×.</p>
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<p>Diameter distribution of sycamore bark fiber bundles.</p>
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<p>Comparison between experimental and predicted composite behavior.</p>
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<p>Numerical tensile curves of sycamore bark fibers.</p>
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17 pages, 3079 KiB  
Article
Determining the Advanced Frequency of Composited Functionally Graded Material Plates Using Third-Order Shear Deformation Theory and Nonlinear Varied Shear Coefficients
by Chih-Chiang Hong
J. Compos. Sci. 2024, 8(8), 325; https://doi.org/10.3390/jcs8080325 - 16 Aug 2024
Viewed by 898
Abstract
The shear effect is usually considered in the numerical calculation of thick composited FGM plates. The characteristics that have the greatest effect on thickness are displacement type, shear correction coefficient, material property and temperature. For the advanced frequency study of thick composited functionally [...] Read more.
The shear effect is usually considered in the numerical calculation of thick composited FGM plates. The characteristics that have the greatest effect on thickness are displacement type, shear correction coefficient, material property and temperature. For the advanced frequency study of thick composited functionally graded material (FGM) plates, it is interesting to consider the extra effects of the nonlinear coefficient c1 term of the third-order shear deformation theory (TSDT) of displacement on the calculation of varied shear correction coefficients. The values of nonlinear shear correction coefficients are usually functions of c1, the power-law exponent parameter and environment temperature. Numerical frequency computations are calculated using a simple homogeneous equation, and are investigated using TSDT and the nonlinear shear correction coefficient for thick composited FGM plates. Results for natural frequencies are found via the functions of length-to-thickness ratio, the power-law exponent parameter, c1 and environment temperature. This novel study in advanced frequency aims to determine the effects of the TSDT and nonlinear shear correction on thick FGM plates under free vibration. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Two-material thick composited FGM plates in environment temperature <span class="html-italic">T.</span></p>
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<p>The process of description derivation for <math display="inline"><semantics> <mrow> <msub> <mi>k</mi> <mi>α</mi> </msub> </mrow> </semantics></math> derivation.</p>
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<p><math display="inline"><semantics> <mrow> <msub> <mi>ω</mi> <mrow> <mn>1</mn> <mi>n</mi> </mrow> </msub> </mrow> </semantics></math> vs. <math display="inline"><semantics> <mrow> <msub> <mi>R</mi> <mi>n</mi> </msub> </mrow> </semantics></math> for: (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>a</mi> <mo>/</mo> <msup> <mi>h</mi> <mo>*</mo> </msup> <mo>=</mo> <mn>5</mn> </mrow> </semantics></math>; (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>a</mi> <mo>/</mo> <msup> <mi>h</mi> <mo>*</mo> </msup> <mo>=</mo> <mn>10</mn> </mrow> </semantics></math>.</p>
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<p><math display="inline"><semantics> <mrow> <msub> <mi>ω</mi> <mrow> <mn>1</mn> <mi>n</mi> </mrow> </msub> </mrow> </semantics></math> vs. <math display="inline"><semantics> <mrow> <msub> <mi>R</mi> <mi>n</mi> </msub> </mrow> </semantics></math> for: (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>a</mi> <mo>/</mo> <msup> <mi>h</mi> <mo>*</mo> </msup> <mo>=</mo> <mn>5</mn> </mrow> </semantics></math>; (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>a</mi> <mo>/</mo> <msup> <mi>h</mi> <mo>*</mo> </msup> <mo>=</mo> <mn>10</mn> </mrow> </semantics></math>.</p>
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<p><math display="inline"><semantics> <mrow> <msub> <mi>ω</mi> <mrow> <mn>1</mn> <mi>n</mi> </mrow> </msub> </mrow> </semantics></math> vs. <math display="inline"><semantics> <mrow> <mo> </mo> <mi>T</mi> </mrow> </semantics></math> for: (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>a</mi> <mo>/</mo> <msup> <mi>h</mi> <mo>*</mo> </msup> <mo>=</mo> <mn>5</mn> </mrow> </semantics></math>; (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>a</mi> <mo>/</mo> <msup> <mi>h</mi> <mo>*</mo> </msup> <mo>=</mo> <mn>10</mn> </mrow> </semantics></math>.</p>
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<p><math display="inline"><semantics> <mrow> <msub> <mi>ω</mi> <mrow> <mn>1</mn> <mi>n</mi> </mrow> </msub> </mrow> </semantics></math> vs. <math display="inline"><semantics> <mrow> <mo> </mo> <mi>T</mi> </mrow> </semantics></math> for: (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>a</mi> <mo>/</mo> <msup> <mi>h</mi> <mo>*</mo> </msup> <mo>=</mo> <mn>5</mn> </mrow> </semantics></math>; (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>a</mi> <mo>/</mo> <msup> <mi>h</mi> <mo>*</mo> </msup> <mo>=</mo> <mn>10</mn> </mrow> </semantics></math>.</p>
Full article ">
20 pages, 4718 KiB  
Article
Buckling Analysis of Variable-Angle Tow Composite Plates through Variable Kinematics Hierarchical Models
by Gaetano Giunta, Domenico Andrea Iannotta, Levent Kirkayak and Marco Montemurro
J. Compos. Sci. 2024, 8(8), 320; https://doi.org/10.3390/jcs8080320 - 13 Aug 2024
Viewed by 1113
Abstract
Variable-Angle Tow (VAT) laminates can improve straight fiber composites’ mechanical properties thanks to the application of curvilinear fibers. This characteristic allows one to achieve ambitious objectives for design and performance purposes. Nevertheless, the wider design space and the higher number of parameters result [...] Read more.
Variable-Angle Tow (VAT) laminates can improve straight fiber composites’ mechanical properties thanks to the application of curvilinear fibers. This characteristic allows one to achieve ambitious objectives for design and performance purposes. Nevertheless, the wider design space and the higher number of parameters result in a more complex structural problem. Among the various approaches that have been used for VAT study, Carrera’s Unified Formulation (CUF) allows one to obtain multiple theories within the same framework, guaranteeing a good compromise between the results’ accuracy and the computational cost. In this article, the linear buckling behavior of VAT laminates is analyzed through the extension of CUF 2D plate models within Reissner’s Mixed Variational Theorem (RMVT). The results show that RMVT can better approximate the prebuckling nonuniform stress field of the plate when compared to standard approaches, thus improving the prediction of the linear buckling loads of VAT composites. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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Figure 1

Figure 1
<p>Plate geometry and reference system.</p>
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<p>Example of in-plane fiber path.</p>
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<p>Acronym system.</p>
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<p>In-plane fiber variation path, case 1.</p>
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<p>Boundary and loading conditions, case 1.</p>
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<p>Contour plots, comparison between the 3LM4 model (<b>left</b>) and Abaqus 3D (<b>right</b>), case 1.</p>
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<p>In-plane fiber path and stacking sequence, case 2.</p>
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<p>Boundary and loading conditions, case 2.</p>
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<p>Buckling modes, compression–shear load <math display="inline"><semantics> <mrow> <msubsup> <mi>P</mi> <mrow> <mi>x</mi> <mi>x</mi> </mrow> <mn>0</mn> </msubsup> <mo>=</mo> <msubsup> <mi>P</mi> <mrow> <mi>x</mi> <mi>y</mi> </mrow> <mn>0</mn> </msubsup> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math> Pa, and comparison between LM2 model (<b>left</b>) and Abaqus 3D (<b>right</b>), case 3.</p>
Full article ">
16 pages, 4709 KiB  
Article
Compression after Impact Response of Kevlar Composites Plates
by Dionysis E. Mouzakis, Panagiotis J. Charitidis and Stefanos P. Zaoutsos
J. Compos. Sci. 2024, 8(8), 299; https://doi.org/10.3390/jcs8080299 - 1 Aug 2024
Viewed by 1140
Abstract
Boeing and Airbus developed a special testing procedure to investigate the compressive response of laminates that have been impacted (following standards ASTM D 7137 and DIN 65561). This study focuses on both experimental and numerical analysis of Kevlar plates subjected to compression after [...] Read more.
Boeing and Airbus developed a special testing procedure to investigate the compressive response of laminates that have been impacted (following standards ASTM D 7137 and DIN 65561). This study focuses on both experimental and numerical analysis of Kevlar plates subjected to compression after impact. To ensure high quality and appropriate mechanical properties, the composite plates were manufactured using autoclaving. The DIN 65561 protocol was followed for all three test systems. Initially, ultrasonic C-scanning was performed on all plates before testing to confirm they were free of any significant defects arising from the manufacturing process. Subsequently, low-energy impact testing was conducted at levels ranging from 0 to 8 Joules. Three specimens were tested at each energy level. After the impact, all specimens underwent ultrasonic C-scanning again to assess the internal delamination damage caused by the impactor. Finally, both pristine and impacted specimens were subjected to compressive testing using the special jig specified in DIN 65561. The compressive impact strength results obtained from these tests were plotted against the delamination area measured by C-scanning. These data were then compared to the results obtained from specimens with artificial damage. Semi-empirical equations were used to fit both sets of curves. The same procedure (impact testing, C-scanning, and data analysis) was repeated to investigate the relationship between impact energy and total delamination area. Lastly, finite element modeling was employed to predict the buckling stresses that develop under compression in the impacted systems studied. These modeling approaches have demonstrated good accuracy in reproducing experimental results for CAI tests. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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Graphical abstract

Graphical abstract
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<p>Kevlar 49/Epoxy cross-ply <math display="inline"><semantics> <mrow> <msub> <mrow> <mfenced close="]" open="["> <mrow> <mn>0</mn> <mo>/</mo> <mn>90</mn> <mo>/</mo> <mo>±</mo> <mn>45</mn> <mo>/</mo> <mn>0</mn> <mo>/</mo> <mn>90</mn> </mrow> </mfenced> </mrow> <mi>s</mi> </msub> </mrow> </semantics></math>.</p>
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<p>Ultrasonic scanning and back wall echo of pristine specimens before compression after impact (CAI) tests.</p>
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<p>In-plane compression and anti-buckle rig, test frame.</p>
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<p>(<b>a</b>) Cohesive interface and (<b>b</b>) Traction–separation law for cohesive interfaces.</p>
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<p>(<b>a</b>) Clamp supported for impact test and (<b>b</b>) Boundary conditions and loading for compression test.</p>
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<p>Optical and C-scan images were obtained after the impact test.</p>
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<p>Observable failures on the surface of the specimens after uniaxial compressive displacement.</p>
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<p>Strength–strain curves obtained from the CAI tests.</p>
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<p>Cumulative Delamination Area vs. Impact Energy.</p>
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<p>CAI Strength–Impact Energy for all specimens.</p>
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<p>CAI Strength vs. Total Delamination Area for all specimens.</p>
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<p>Finite element model with 8112 elements.</p>
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<p>Useful comparison between experimental strength (averaged) and FEA CAI strain–strength results.</p>
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27 pages, 11196 KiB  
Article
Mechanical Characterization of GFRP Tiled Laminates for Structural Engineering Applications: Stiffness, Strength and Failure Mechanisms
by Jordi Uyttersprot, Wouter De Corte and Wim Van Paepegem
J. Compos. Sci. 2024, 8(7), 265; https://doi.org/10.3390/jcs8070265 - 8 Jul 2024
Cited by 1 | Viewed by 1251
Abstract
This study investigates the mechanical properties of tiled laminates, frequently used in FRP bridges, and a completely new class of composites for which currently no experimental literature is available. In this paper, first a microscopic examination of laminates extracted from bridge deck flanges [...] Read more.
This study investigates the mechanical properties of tiled laminates, frequently used in FRP bridges, and a completely new class of composites for which currently no experimental literature is available. In this paper, first a microscopic examination of laminates extracted from bridge deck flanges is performed, revealing complex multi-ply structures and tiled laminates in the transverse direction of the bridge deck. The subsequent fabrication of tiled laminates in the transverse (i.e., weak) and longitudinal (i.e., strong) span direction explores stiffness and strength characteristics depending on the stacking angle. It is observed that the stiffness in both directions is only slightly reduced with increasing stacking angles, reaching a maximum decrease of 10%, while the failure strength is significantly reduced, particularly with longitudinal tiling, dropping by approximately 70% for a 2° stacking angle. Transverse tiling demonstrates a more moderate 45% strength reduction due to the presence of some 90° plies. Given the small reduction in the stiffness and the fact that in many applications the design is mainly governed by serviceability (i.e., stiffness) requirements than strength, this strength reduction may be acceptable, considering other advantages of the concept. Additionally, this research sheds light on failure mechanisms, emphasizing the role of ply assembly in stress distribution and highlighting the importance of gradual ply ends in reducing strain concentrations. These findings provide valuable insights for optimizing tiled laminates in structural applications, ensuring their effective and reliable use. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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Figure 1

Figure 1
<p>Delamination propagation (red arrows) in a traditional composite sandwich panel with plane parallel laminate skin and a tiled sandwich panel with tiled laminate during and accidental damage (blue lines).</p>
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<p>Test setup uniaxial tensile test and DIC with inset of the sample speckle pattern.</p>
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<p>Reference axes of an oriented ply abcd (1, 2) relative to global lamination axes (x, y) (plane ABCD) [<a href="#B13-jcs-08-00265" class="html-bibr">13</a>].</p>
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<p>Internal orientation of the fiber plies in a tiled GFRP web–core sandwich footbridge.</p>
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<p>Transverse cross-section (TL laminate) with Close-ups 1 and 2.</p>
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<p>Longitudinal cross-section (PP laminate) with Close-ups 1 and 2.</p>
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<p>Graphical illustration of the laminate lay-up at the flange–web connection in the transverse and longitudinal direction of the laminate in the top and bottom flange of a web–core sandwich panel bridge deck.</p>
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<p>45°, 0° and 90° coupons (<b>top</b>) and associated top (<b>middle</b>) and edge view (<b>bottom</b>) of the failure behavior.</p>
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<p>Top flange transverse specimen with no (<b>a</b>), one (<b>b</b>,<b>c</b>) and two (<b>d</b>) webs.</p>
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<p>Tensile test setup with extensometer and strain gauges at the front and back.</p>
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<p>Overview of the tensile strength (<b>left</b>) and Young’s modulus (<b>right</b>) of the top and bottom flange for the different types of specimens.</p>
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<p>Failure behavior of transverse specimens with no (0 W), one (1 W) and two webs (2 W).</p>
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<p>Laminate construction and lay-up of the PP reference specimens including cutting lines.</p>
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<p>Laminate construction and lay-up of the TL specimens including cutting lines.</p>
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<p>Graphical representation of the manufacturing of a gradual TL using an edge strip.</p>
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<p>Stress–strain data of the tensile tests on the PP reference and TL specimens with a 2° and 4° stacking angle.</p>
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<p>Failure behavior of the PP reference (<b>a</b>), TL specimens (<b>b</b>) and a close-up of the interlaminar failure between the plies of a TL (<b>c</b>).</p>
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<p>Full-field strain image (red highest strain and purple lowest strain) and DIC strain evolution over the centerline for the TL2° (<b>left</b>) and TL4° (<b>right</b>) specimens.</p>
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<p>Geometry (in mm) and laminate construction of the PP reference and TL specimens.</p>
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<p>Local Young’s modulus along the centerline of the PP reference and TL specimens.</p>
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<p>Average stress–strain data of the PP and TL specimens (shifted every 0.2%).</p>
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<p>Relative Young’s modulus in function of the theoretical stacking angle.</p>
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<p>Failure behavior for a PP (<b>left</b>), TL1t1 (<b>center</b>) and TL3t1 (<b>right</b>) specimen.</p>
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<p>Online microscopic images of the failure mechanism in TL2t1 at the location of an overlap and ply start/end (<b>a</b>) with the green lines indicating one ply stack; the propagation of the crack due to shear stresses (<b>b</b>–<b>d</b>), culminating in the ultimate failure (<b>e</b>).</p>
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<p>Microscopic close-ups of failure onset in specimen TL2t1 at the location of a ply end/beginning with larger (<b>a</b>) and smaller (<b>b</b>) laminate thickness due to ply stacking.</p>
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<p>Full-field strain image and evolution over the centerline for the PP reference and the different types of TL specimens.</p>
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<p>Overall mean microstrain interval and average strain for the PP reference and the different types of TL specimens.</p>
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<p>Comparison between the stiffness (circle) and LPF strength (square) relative to a PP laminate for a tiled laminate in the longitudinal (black) and transverse (white) direction with trendlines (dotted lines).</p>
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11 pages, 5719 KiB  
Article
Towards 3D Pore Structure of Porous Gypsum Cement Pozzolan Ternary Binder by Micro-Computed Tomography
by Girts Bumanis, Laura Vitola, Xiangming Zhou, Danutė Vaičiukynienė and Diana Bajare
J. Compos. Sci. 2024, 8(7), 264; https://doi.org/10.3390/jcs8070264 - 8 Jul 2024
Viewed by 1089
Abstract
A sophisticated characterisation of a porous material structure has been challenging in material science. Three-dimensional (3D) structure analysis allows the evaluation of a material’s homogeneity, pore size distribution and pore wall properties. Micro-computed tomography (micro-CT) offers a non-destructive test method for material evaluation. [...] Read more.
A sophisticated characterisation of a porous material structure has been challenging in material science. Three-dimensional (3D) structure analysis allows the evaluation of a material’s homogeneity, pore size distribution and pore wall properties. Micro-computed tomography (micro-CT) offers a non-destructive test method for material evaluation. This paper characterises a novel ternary binder’s porous structure using micro-CT. Gypsum–cement–pozzolan (GCP) ternary binders are low-carbon footprint binders. Both natural and industrial gypsum were evaluated as a major components of GCP binders. Porous GCP binder was obtained by a foaming admixture, and the bulk density of the material characterised ranged from 387 to 700 kg/m3. Micro-CT results indicate that pores in the range from 0.017 to 3.0 mm can be effectively detected and described for porous GCP binders. The GCP binder structure proved to be dominant by 0.1 to 0.2 mm micropores. For GCP binders produced with natural gypsum, macropores from 2.2 to 2.9 mm are formed, while GCP binders with phosphogypsum possess pores from 0.2 to 0.6 mm. Micro-CT proved to be an effective instrument for characterising the homogeneity and hierarchical pore structure of porous ternary binders. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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Figure 1
<p>Macrostructure of the porous GCP material at 40× magnification. (<b>a</b>) G1; (<b>b</b>) P1; (<b>c</b>) G2; (<b>d</b>) P2.</p>
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<p>Reconstruction of pore structure of the GCP binder samples: (<b>a</b>) GCP binder mixture composition G1; (<b>b</b>) G2; (<b>c</b>) P1; (<b>d</b>) P2.</p>
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<p>Three-dimensional (3D) model of segmented pore structure of the GCP binders: (<b>a</b>) G1; (<b>b</b>) G2; (<b>c</b>) P1; (<b>d</b>) P2.</p>
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<p>Cross-sections of porous GCP binders. (<b>a</b>) G1; (<b>b</b>) G2; (<b>c</b>) P1; (<b>d</b>) P2.</p>
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<p>Pore size distribution of porous GCP.</p>
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11 pages, 2286 KiB  
Article
Mechanical Properties and Thermal Conductivity of Y-Si and Gd-Si Silicides: First-Principles Calculations
by Kexue Peng, Panxin Huang, Guifang Han, Huan Liu, Weibin Zhang, Weili Wang and Jingde Zhang
J. Compos. Sci. 2024, 8(6), 221; https://doi.org/10.3390/jcs8060221 - 12 Jun 2024
Viewed by 882
Abstract
The traditional Si bonding layer in environmental barrier coatings has a low melting point (1414 °C), which is a significant challenge in meeting the requirements of the next generation higher thrust-to-weight ratio aero-engines. To seek new bonding layer materials with higher melting points, [...] Read more.
The traditional Si bonding layer in environmental barrier coatings has a low melting point (1414 °C), which is a significant challenge in meeting the requirements of the next generation higher thrust-to-weight ratio aero-engines. To seek new bonding layer materials with higher melting points, the mechanical properties of Y-Si and Gd-Si silicides were calculated by the first-principles method. Subsequently, empirical formulae were employed to compute the sound velocities, Debye temperatures, and the minimum coefficients of thermal conductivity for the YSi, Y5Si4, Y5Si3, GdSi, and Gd5Si4. The results showed that Y5Si4 has the best plasticity and ductility among all these materials. In addition, Gd5Si4 has the minimum Debye temperature (267 K) and thermal conductivity (0.43 W m−1 K−1) compared with others. The theoretical calculation results indicate that some silicides in the Y-Si and Gd-Si systems possess potential application value in high-temperature bonding layers for thermal and/or environmental barrier coating. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Crystal structures of Y<sub>x</sub>Si<sub>y</sub> and Gd<sub>x</sub>Si<sub>y</sub>: (<b>a</b>) YSi, (<b>b</b>) Y<sub>5</sub>Si<sub>4</sub>, (<b>c</b>) Y<sub>5</sub>Si<sub>3</sub>, (<b>d</b>) GdSi, (<b>e</b>) Gd<sub>5</sub>Si<sub>4</sub> (the blue-colored ball represented Si atoms, the green-colored ball represented Y atoms and the purple-colored ball represented Gd atoms).</p>
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<p>Relative errors of lattice constants of Y<sub>x</sub>Si<sub>y</sub> and Gd<sub>x</sub>Si<sub>y</sub>.</p>
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<p>Surface contour of direction-dependent Young’s modulus (<b>a</b>) YSi, (<b>b</b>) Y<sub>5</sub>Si<sub>4</sub>, (<b>c</b>) Y<sub>5</sub>Si<sub>3</sub>, (<b>d</b>) GdSi, (<b>e</b>) Gd<sub>5</sub>Si<sub>4</sub>, (<b>a1</b>–<b>e1</b>) are planar projections on (100), (010), and (001) crystallographic planes.</p>
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<p>Comparison of the calculated Debye temperature of Y<sub>x</sub>Si<sub>y</sub> and Gd<sub>x</sub>Si<sub>y</sub> with reference values [<a href="#B43-jcs-08-00221" class="html-bibr">43</a>,<a href="#B44-jcs-08-00221" class="html-bibr">44</a>,<a href="#B45-jcs-08-00221" class="html-bibr">45</a>,<a href="#B46-jcs-08-00221" class="html-bibr">46</a>,<a href="#B47-jcs-08-00221" class="html-bibr">47</a>].</p>
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<p>Relationship of thermal conductivity with temperature for (<b>a</b>) Y<sub>x</sub>Si<sub>y</sub> and (<b>b</b>) Gd<sub>x</sub>Si<sub>y</sub>. Solid line represents the minimum value of thermal conductivity.</p>
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16 pages, 7979 KiB  
Article
Physical, Mechanical and Microstructural Characteristics of Perlite-Based Geopolymers Modified with Mineral Additives
by Natalia I. Kozhukhova, Roman A. Glazkov, Marina S. Ageeva, Marina I. Kozhukhova, Ivan S. Nikulin and Irina V. Zhernovskaya
J. Compos. Sci. 2024, 8(6), 211; https://doi.org/10.3390/jcs8060211 - 4 Jun 2024
Cited by 1 | Viewed by 1211
Abstract
One of the promising raw materials for the synthesis of geopolymers is perlite, which is a natural low-calcium aluminosilicate. This research studied the physical, mechanical and microstructural characteristics of perlite-based geopolymers modified with different mineral additives that were prepared using different methods of [...] Read more.
One of the promising raw materials for the synthesis of geopolymers is perlite, which is a natural low-calcium aluminosilicate. This research studied the physical, mechanical and microstructural characteristics of perlite-based geopolymers modified with different mineral additives that were prepared using different methods of introducing the alkali components and curing conditions. The experimental results of the consolidated perlite-based geopolymer pastes showed that curing conditions and the method of introducing the alkali component into the geopolymer matrix had a minimal effect on the average density while demonstrating a significant boost in compressive strength. So, after thermal treatment, the compressive strength increased by 0.63 to 11.4 times for the mixes when fresh alkali solution was used and by 0.72 to 12.8 times for the mixes with the 24 h conditioned alkali solution. Maximum-strength spikes from 1.1 MPa to 13.2 MPa and from 0.7 MPa to 9.7 MPa were observed for the mixes with kaolin when prepared with fresh and conditioned alkali solutions, respectively. It was also observed that thermal treatment facilitates the compaction of the matrix structure by 18% and 1% for the non-modified mix and the mix modified with Portland cement. Perlite-based geopolymers modified with Portland cement and citrogypsum demonstrated a significant reduction in the initial and final setting times with both methods of introducing the alkali solution. On the surface of mixes modified with citrogypsum, regardless of the curing conditions and method of introducing the alkali component, an efflorescence substance was observed. The microstructural analysis of the consolidated geopolymer perlite-based pastes containing citrogypsum demonstrated a loose structure and the presence of efflorescence, which can be associated with a retardation in interaction processes between alkali cations and the aluminosilicate component. EDS analysis demonstrated that the presence of such elements as oxygen, sodium and sulfur may indicate the efflorescence of unreacted sodium hydroxide (NaOH), citrogypsum (CaSO4) and the products of their interaction in the form of crystalline hydrates of sodium sulfate (Na2SO4). Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Used mineral raw materials (<b>a</b>) P (perlite); (<b>b</b>) K (kaolin); (<b>c</b>) MK (metakaolin); (<b>d</b>) PC (Portland cement); (<b>e</b>) CG (citrogypsum).</p>
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<p>Microstructure of perlite after grinding in a ball mill (SSA = 482.2 m<sup>2</sup>/kg) at different resolution: (<b>a</b>) ×500; (<b>b</b>) ×3000; (<b>c</b>) ×10,000; (<b>d</b>) ×25,000.</p>
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<p>Microstructure of perlite after grinding in a ball mill (SSA = 482.2 m<sup>2</sup>/kg) at different resolution: (<b>a</b>) ×500; (<b>b</b>) ×3000; (<b>c</b>) ×10,000; (<b>d</b>) ×25,000.</p>
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<p>Physical and mechanical characteristics of perlite-based geopolymer pastes with different mineral modifiers after (<b>a</b>) treatment in ambient conditions and (<b>b</b>) thermal treatment at 70 °C.</p>
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<p>Appearance of perlite-based geopolymer pastes with different mineral modifiers after curing in ambient conditions: (<b>a</b>) PGP; (<b>b</b>) P-PC; (<b>c</b>) P-K; (<b>d</b>) P-MK; (<b>e</b>) P-CG. 1—fresh alkali solution; 2—24 h conditioned alkali solution. <span class="html-italic">Note: this image was made 30 min after molding procedure</span>.</p>
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<p>Efflorescence substance on the surface of mix P-CG, activated with (<b>a</b>) fresh alkali solution; (<b>b</b>) 24 h conditioned alkali solution. Treatment type—ambient conditions.</p>
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<p>Appearance of perlite-based geopolymer pastes with different mineral modifiers after thermal treatment at 70 °C: (<b>a</b>) PGP; (<b>b</b>) P-PC; (<b>c</b>) P-K; (<b>d</b>) P-MK; (<b>e</b>) P-CG. Upper level—fresh alkali solution; lower level—24 h conditioned alkali solution.</p>
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<p>Microstructure of perlite-based geopolymer mixes.</p>
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<p>Microstructure of perlite-based geopolymer mixes.</p>
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<p>EDS spectra of efflorescence components taken from the surface of P-CG mix, cured (<b>a</b>) in ambient conditions; (<b>b</b>,<b>c</b>) with thermal treatment.</p>
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26 pages, 5470 KiB  
Article
Metaheuristic Optimization of Functionally Graded 2D and 3D Discrete Structures Using the Red Fox Algorithm
by J. S. D. Gaspar, M. A. R. Loja and J. I. Barbosa
J. Compos. Sci. 2024, 8(6), 205; https://doi.org/10.3390/jcs8060205 - 30 May 2024
Cited by 1 | Viewed by 780
Abstract
The growing applicability of functionally graded materials is justified by their ability to contribute to the development of advanced solutions characterized by the material customization, through the selection of the best parameters that will confer the best mechanical behaviour for a given structure [...] Read more.
The growing applicability of functionally graded materials is justified by their ability to contribute to the development of advanced solutions characterized by the material customization, through the selection of the best parameters that will confer the best mechanical behaviour for a given structure under specific operating conditions. The present work aims to attain the optimal design solutions for a set of illustrative 2D and 3D discrete structures built from functionally graded materials using the Red Fox Optimization Algorithm, where the design variables are material parameters. From the results achieved one concludes that the optimal selection and distribution of the different materials’ mixture and the different exponents associated with the volume fraction law significantly influence the optimal responses found. To note additionally the good performance of the coupling between this optimization technique and the finite element method used for the linear static and free vibration analyses. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Schematic Representation of a Structure Built in FGM with a Variation in Properties as a Function of the Structure’s Height.</p>
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<p>Quadratic Beam Element and its Degrees of Freedom.</p>
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<p>Schematic diagram representation of the interaction between the finite element calculation and the optimization algorithm in the one-design variable model.</p>
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<p>Schematic diagram representation of the interaction between the finite element calculation and the optimization algorithm in the four-design variable model.</p>
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<p>Flowchart of the Red Fox Algorithm.</p>
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<p>Schematic Representation of 2D Truss.</p>
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<p>Minimum Discretization of Two-dimensional Truss.</p>
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<p>Evolution of the Young’s Modulus of the 2D Truss for the Optimal Solution Found for Minimizing the Maximum Resulting Displacement using One Design Variable.</p>
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<p>Evolution of the Young’s Modulus of the 2D Truss for the Optimal Solution Found for Maximizing the Fundamental Frequency using the One Design Variable.</p>
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<p>(<b>a</b>) Schematic Representation of 2D Frame; (<b>b</b>) Minimum 2D Frame Discretization.</p>
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<p>Evolution of the Modulus of Elasticity of the 2D Frame by the Best Solution Found for Minimizing the Maximum Resulting Displacement using One Design Variable.</p>
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<p>Evolution of the Modulus of Elasticity of the 2D Frame by the Best Solution Found for Maximizing the Fundamental Frequency with One Design Variable.</p>
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<p>Schematic representation of three-dimensional structure under downward load.</p>
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<p>Evolution of the Young’s Modulus of the 3D Truss for the Best Solution Found for Minimizing the Maximum Resulting Displacement using One Design Variable.</p>
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<p>Evolution of the Young’s Modulus of the 3D Truss for the Best Solution Found for Maximizing the Fundamental Frequency using One Design Variable.</p>
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<p>Three-dimensional Frame.</p>
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<p>Evolution of the Modulus of Elasticity of the 3D Frame for the Best Solution Found for Minimizing the Maximum Resulting Displacement using One Design Variable.</p>
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<p>Evolution of the Young’s Modulus of the 3D Frame for the Best Solution Found for Maximizing Natural Frequency using One Design Variable.</p>
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<p>Evolution of Young’s Modulus of the 2D Frame for the Best Solution found for Minimizing the Maximum Resulting Displacement using four Design Variables.</p>
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<p>Evolution of Young’s Modulus of 2D Frame for the Best Solution found for Maximizing Natural Frequency using four Design Variables.</p>
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<p>Evolution of Young’s Modulus of the 3D Frame for the Best Solution for Minimizing the Maximum Resulting Displacement using Four Design Variables.</p>
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<p>Evolution of Young’s Modulus of the 3D Frame for the Best Solution Found for Maximizing the Fundamental Frequency using Four Design Variables.</p>
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20 pages, 57487 KiB  
Article
Impact Performance of 3D Orthogonal Woven Composites: A Finite Element Study on Structural Parameters
by Wang Xu, Mohammed Zikry and Abdel-Fattah M. Seyam
J. Compos. Sci. 2024, 8(6), 193; https://doi.org/10.3390/jcs8060193 - 21 May 2024
Cited by 2 | Viewed by 1222
Abstract
This study uses the finite element method (FEM) to investigate the effect of key structural parameters on the impact resistance of E-glass 3D orthogonal woven (3DOW) composites subjected to low-velocity impact. These structural parameters include the number of y-yarn layers, the path of [...] Read more.
This study uses the finite element method (FEM) to investigate the effect of key structural parameters on the impact resistance of E-glass 3D orthogonal woven (3DOW) composites subjected to low-velocity impact. These structural parameters include the number of y-yarn layers, the path of the binder yarn (z-yarn), and the density of the x-yarn. Using ABAQUS, yarn-level finite element (FE) models are created based on the measured geometrical parameters and validated for energy absorption and damage behavior from experimental data gathered from the previous study. The results from finite element analysis (FEA) indicate that the x-yarn density and the binder path substantially influenced the composites’ damage behavior and impact performance. Increasing x-yarn density in 3DOW leads to a 15% increase in energy absorption compared to models with reduced x-yarn densities. Moreover, as the x-yarn density increases, crack lengths at the back face of the resin matrix decrease in the y-yarn direction but increase in the x-yarn direction. The basket weave structure absorbs less energy than plain and 2 × 1 twill structures due to the less constrained weft primary yarns. These results underscore the importance of these structural parameters in optimizing 3DOW composite for better impact performance, providing valuable insights for the design of advanced composite structures. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Finite element model of 3DOW composite.</p>
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<p>Mesh sensitivity study for 3DOW composite.</p>
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<p>Logic Flow of deformation, damage initiation, damage progression, and element deletion in VUMAT.</p>
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<p>Experimental and numerical load–time curve comparison for (<b>a</b>) 2L487, (<b>b</b>) 2L545, and (<b>c</b>) 2L587.</p>
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<p>Experimental and numerical load–time curve comparison for (<b>a</b>) 2LTwill and (<b>b</b>) 2LBasket.</p>
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<p>Energy absorption comparison from finite element analysis in 2-, 3-, and 4-layer 3DOW with varying x-yarn densities.</p>
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<p>Internal energy absorption in primary and secondary yarns of (<b>a</b>) 2-layer, (<b>b</b>) 3-layer, and (<b>c</b>) 4-layer 3DOW.</p>
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<p>Damage contour of 2-layer 3DOW under 4.4 m/s impact at t = 1 ms: (<b>a</b>) face fiber compressive damage for 2L487; (<b>b</b>) back fiber tensile damage for 2L487; (<b>c</b>) face fiber compressive damage for 2L545; (<b>d</b>) back fiber tensile damage for 2L545; (<b>e</b>) face fiber compressive damage for 2L587; (<b>f</b>) back fiber tensile damage for 2L587.</p>
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<p>Damage propagation on back face of resin matrix for (<b>a</b>) 2L487, (<b>b</b>) 2L545, and (<b>c</b>) 2L587.</p>
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<p>(<b>a</b>) Internal energy absorption of 2-layer 3DOW with different binder yarn paths, (<b>b</b>) internal energy distribution in primary and secondary yarns of 3DOW.</p>
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<p>Yarn breakage locations in (<b>a</b>) 2LPlain, (<b>b</b>) 2LTwill, and (<b>c</b>) 2LBasket.</p>
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<p>Damage propagation on back face of resin matrix for (<b>a</b>) 2LPlain, (<b>b</b>) 2LTwill, and (<b>c</b>) 2LBasket.</p>
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17 pages, 52966 KiB  
Article
Mechanical Analysis and Simulation of Wood Textile Composites
by Claudia L. von Boyneburgk, Dimitri Oikonomou, Werner Seim and Hans-Peter Heim
J. Compos. Sci. 2024, 8(5), 190; https://doi.org/10.3390/jcs8050190 - 18 May 2024
Cited by 1 | Viewed by 1069
Abstract
Wood Textile Composites (WTCs) represent a new and innovative class of materials in the field of natural fiber composites. Consisting of fabrics made from willow wood strips (Salix americana) and polypropylene (PP), this material appears to be particularly suitable for structural [...] Read more.
Wood Textile Composites (WTCs) represent a new and innovative class of materials in the field of natural fiber composites. Consisting of fabrics made from willow wood strips (Salix americana) and polypropylene (PP), this material appears to be particularly suitable for structural applications in lightweight construction. Since the threads of the fabric are significantly oversized compared to classic carbon or glass rovings, fundamental knowledge of the mechanical properties of the material is required. The aim of this study was to investigate whether WTCs exhibit classic behavior in terms of fiber composite theory and to classify them in relation to comparable composite materials. It was shown that WTCs meet all the necessary conditions for fiber-reinforced composites in tensile, bending, and compression tests and can be classified as natural-fiber-reinforced polypropylene composites. In addition, it was investigated whether delamination between the fiber and matrix can be simulated by using experimentally determined mechanical data as input. Using finite element analysis (FEA), it was shown that the shear stress components of a stress tensor in the area of the interface between the fiber and matrix are responsible for delamination in the composite material. It was also shown that the resistance to shear stress depends on the geometric conditions of the reinforcing fabric. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Wood Textile Composites (WTCs) including close-up of the cross-section.</p>
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<p>Set-up of the compression test.</p>
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<p>Set-up of the short-beam shear test.</p>
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<p>Illustration of a unit cell of the WTC using the simulation software Marc-Mentat. (Version 2021.1).</p>
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<p>(<b>a</b>) Results of the tensile test: tensile strength and Young’s modulus of WTC 0°, WTC 90°, polypropylene, willow strips 0°, and solid willow 90°; (<b>b</b>) results of the tensile test: stress–strain diagrams of WTC 0°, WTC 90°, polypropylene, willow strips 0°, and solid willow 90.</p>
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<p>(<b>a</b>) SEM image of the fracture surface of the tensile test specimen (0°), 23× magnification; (<b>b</b>) SEM image of the fracture surface of the tensile test specimen (90°), 25× magnification.</p>
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<p>(<b>a</b>) Results of the three-point-bending test: three-point-bending strength and flexural modulus of WTC 0° and WTC 90°, polypropylene, and solid willow 0° and 90°; (<b>b</b>) results of the three-point-bending test: stress–strain diagrams of WTC 0° and WTC 90°, polypropylene, and solid willow 0° and 90°.</p>
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<p>(<b>a</b>) Results of the compression test: compressive strength and compressive modulus of WTC 0° and WTC 90°, polypropylene, and willow 0° and 90°; (<b>b</b>) results of the compression test: stress–strain diagrams WTC 0° and WTC 90°, polypropylene, and willow 0° and 90°.</p>
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<p>(<b>a</b>) SEM image of a WTC test specimen after compression test in the main fiber direction (0°), 29× magnification; (<b>b</b>) SEM image of a WTC test specimen after the compression test in the main fiber direction (0°), 500× magnification.</p>
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<p>(<b>a</b>) Overview image of a test specimen after short-beam shear test according to DIN EN ISO 14130, 20× magnification; (<b>b</b>) detailed image of the same test specimen, 50× magnification; (<b>c</b>) detailed image of a test specimen after short-beam shear test according to ASTM D2344, 80× magnification.</p>
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<p>(<b>a</b>) Visualization of delamination by “Adhesion deactivation” in Marc-Mentat; (<b>b</b>) selected positions for detailed examination of delamination.</p>
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<p>Simulated shear stress as a function of the increment number.</p>
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<p>Visualization of the simulated shear stress in Marc-Mentat at increment 25.</p>
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14 pages, 1697 KiB  
Article
Analysis of Intact/Delaminated Composite and Sandwich Beams Using a Higher-Order Modeling Technique
by Yuan Feng, Abdul Hamid Sheikh and Guanzhen Li
J. Compos. Sci. 2024, 8(5), 175; https://doi.org/10.3390/jcs8050175 - 10 May 2024
Cited by 1 | Viewed by 1178
Abstract
A simple higher-order model (HOM) is presented in this study for the bending analysis of an intact or delaminated composite and sandwich beam. This model adopts the concept of sub-laminates to simulate multilayered structures, and each sub-laminate takes cubic variation for axial displacement [...] Read more.
A simple higher-order model (HOM) is presented in this study for the bending analysis of an intact or delaminated composite and sandwich beam. This model adopts the concept of sub-laminates to simulate multilayered structures, and each sub-laminate takes cubic variation for axial displacement and linear variation for transverse displacement through the thickness. A sub-laminate possesses displacement components at its surfaces (bottom and top) that provide a straightforward way to improve the accuracy of prediction by stacking several sub-laminates. Thus, analysts will have the flexibility to balance the computational cost and the accuracy by selecting an appropriate sub-lamination scheme. The proposed model was implemented by developing a C0 beam element that has only displacement unknowns. The model was used to solve numerical examples of composite and sandwich beams to demonstrate its performance. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>(<b>a</b>) One-layer model; (<b>b</b>) layer-wise like model; (<b>c</b>) sub-laminate model.</p>
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<p>Higher-order model (HOM)-based sub-laminate.</p>
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<p>Modeling of delaminated region.</p>
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<p>Through-thickness variation of (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mover accent="true"> <mrow> <mi>σ</mi> </mrow> <mo stretchy="false">¯</mo> </mover> </mrow> <mrow> <mi>x</mi> <mi>x</mi> </mrow> </msub> </mrow> </semantics></math>, and (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mover accent="true"> <mrow> <mi>τ</mi> </mrow> <mo stretchy="false">¯</mo> </mover> </mrow> <mrow> <mi>x</mi> <mi>z</mi> </mrow> </msub> </mrow> </semantics></math> for the symmetrical composite beams predicted at the beam midspan by different models [<a href="#B11-jcs-08-00175" class="html-bibr">11</a>,<a href="#B49-jcs-08-00175" class="html-bibr">49</a>].</p>
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<p>A cantilever laminated beam [0/90/0/90]<sub>s</sub> with single delamination under a point load.</p>
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<p>Variation of transverse displacement captured at surfaces above and below the delamination.</p>
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12 pages, 8727 KiB  
Communication
Comprehensive Composite Mould Filling Pattern Dataset for Process Modelling and Prediction
by Boon Xian Chai, Jinze Wang, Thanh Kim Mai Dang, Mostafa Nikzad, Boris Eisenbart and Bronwyn Fox
J. Compos. Sci. 2024, 8(4), 153; https://doi.org/10.3390/jcs8040153 - 18 Apr 2024
Cited by 22 | Viewed by 1661
Abstract
The Resin Transfer Moulding process receives great attention from both academia and industry, owing to its superior manufacturing rate and product quality. Particularly, the progression of its mould filling stage is crucial to ensure a complete reinforcement saturation. Contemporary process simulation methods focus [...] Read more.
The Resin Transfer Moulding process receives great attention from both academia and industry, owing to its superior manufacturing rate and product quality. Particularly, the progression of its mould filling stage is crucial to ensure a complete reinforcement saturation. Contemporary process simulation methods focus primarily on physics-based approaches to model the complex resin permeation phenomenon, which are computationally expensive to solve. Thus, the application of machine learning and data-driven modelling approaches is of great interest to minimise the cost of process simulation. In this study, a comprehensive dataset consisting of mould filling patterns of the Resin Transfer Moulding process at different injection locations for a composite dashboard panel case study is presented. The problem description and significance of the dataset are outlined. The distribution of this comprehensive dataset aims to lower the barriers to entry for researching machine learning approaches in composite moulding applications, while concurrently providing a standardised baseline for evaluating newly developed algorithms and models in future research works. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Schematic diagram depicting a typical composite mould filling process. (This image was previously published in [<a href="#B26-jcs-08-00153" class="html-bibr">26</a>]).</p>
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<p>The investigated dashboard panel and its permeability profile.</p>
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<p>The 576 potential resin injection locations (yellow dots) on the mould surface projected on an (x, y) plane. (This image was previously published in [<a href="#B26-jcs-08-00153" class="html-bibr">26</a>]).</p>
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<p>Schematic diagram of the experimental mould filling setup. Some stains are present on the exterior of the mould, due to mould reusing, which do not affect the process. (This image was previously published in [<a href="#B26-jcs-08-00153" class="html-bibr">26</a>]).</p>
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<p>Example of a mould filling pattern and its time scale (central resin injection, Image 277).</p>
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<p>Resin injection from the top left corner of the mould, with the injection gate positioned at (1, 24), shown in Image 1 of the dataset.</p>
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<p>Resin injection from the top right corner of the mould, with the injection gate positioned at (24, 1), shown in Image 24 of the dataset.</p>
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<p>Resin injection from the bottom left corner of the mould, with the injection gate positioned at (1, 1), shown in Image 553 of the dataset.</p>
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<p>Resin injection from the bottom right corner of the mould, with the injection gate positioned at (24, 24), shown in Image 576 of the dataset.</p>
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11 pages, 2944 KiB  
Article
The Morphological and Thermal Characteristics of Hollow-Glass-Microsphere-Coated Phase Change Material–Cow Pie Embedded Recycled Plastic Tiles for Cool Roofs
by S. Krishna Satya and P. S. Rama Sreekanth
J. Compos. Sci. 2024, 8(4), 148; https://doi.org/10.3390/jcs8040148 - 13 Apr 2024
Viewed by 1920
Abstract
This study addresses the global plastic waste crisis and the urban heat island effect by developing an innovative solution: recycled plastic roof tiles embedded with phase change material (PCM) and coated with hollow-glass-microsphere-based white paint. The samples were fabricated with cow pie fibers, [...] Read more.
This study addresses the global plastic waste crisis and the urban heat island effect by developing an innovative solution: recycled plastic roof tiles embedded with phase change material (PCM) and coated with hollow-glass-microsphere-based white paint. The samples were fabricated with cow pie fibers, OM37 and OM42 PCM materials with different wt./vol. values, i.e., 15/50, 20/50, 25/50, 30/50 ratios. The fabricated tiles were coated with hollow glass microspheres to provide a reflective layer. The tiles’ effectiveness was evaluated through morphological examination and thermal analysis. The SEM analysis revealed an excellent bonding ability for the PCM blend, i.e., OM37 and OM42 at a 20/50 ratio (wt./vol.) with cow pie fibers. Adding cow pie fibers to the PCM shifted the melting points of OM37 and OM42, indicating an increased heat storage capacity in both blends. The thermal conductivity results revealed decreased thermal conductivity with an increased cow pie fiber percentage. The recycled plastic roof tile of the PCM composite at a 20/50 (wt./vol.) ratio showed good thermal properties. Upon testing in real-time conditions in a physical setup, the roof tiles showed a temperature reduction of 8 °C from outdoors to indoors during the peak of summer. In winter, cozy temperatures were maintained indoors due to the heat regulation from the roof. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Schematic flowchart of the preparation of novel recycled plastic roof tiles.</p>
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<p>SEM images of (<b>a</b>) pure cow pie powder at 100 μm magnification; (<b>b</b>) OM37 blend PCM at a 20/50 ratio at 200 μm magnification; (<b>c</b>) OM42 blend at a 20/50 ratio at 200 μm magnification; (<b>d</b>) pure cow pie powder at 500 μm magnification; (<b>e</b>) OM37 blend at 20/50 ratio at 500 μm magnification; (<b>f</b>) OM42 blend at 20/50 ratio at 500 μm magnification.</p>
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<p>XRD graphs of OM37 and OM42 blends.</p>
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<p>DSC curves of (<b>a</b>) OM37 blend and (<b>b</b>) OM42 blend.</p>
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<p>(<b>a</b>) Coefficient of thermal expansion, (<b>b</b>) thermal conductivity, (<b>c</b>) volumetric heat capacity.</p>
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<p>(<b>a</b>) Physical setup built for testing the tiles; (<b>b</b>) temperature measurement using a thermocouple.</p>
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<p>Real-time temperature distribution of recycled plastic roof tiles in (<b>a</b>) summer (May), (<b>b</b>) rainy (August), and (<b>c</b>) winter (December) seasons.</p>
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17 pages, 8050 KiB  
Article
A Numerical Assessment of the Influence of Local Stress Ratio in the Fatigue Analysis of Post-Buckled Composite Single-Stringer Specimen
by Antonio Raimondo and Chiara Bisagni
J. Compos. Sci. 2024, 8(4), 143; https://doi.org/10.3390/jcs8040143 - 11 Apr 2024
Cited by 2 | Viewed by 1609
Abstract
This paper presents a numerical approach for investigating fatigue delamination propagation in composite stiffened panels loaded in compression in the post-buckling field. These components are widely utilized in aerospace structures due to their lightweight and high-strength properties. However, fatigue-induced damage, particularly delamination at [...] Read more.
This paper presents a numerical approach for investigating fatigue delamination propagation in composite stiffened panels loaded in compression in the post-buckling field. These components are widely utilized in aerospace structures due to their lightweight and high-strength properties. However, fatigue-induced damage, particularly delamination at the skin–stringer interface, poses a significant challenge. The proposed numerical approach, called the “Min–Max Load Approach”, allows for the calculation of the local stress ratio in a single finite element analysis. It represents the ratio between the minimum and maximum values of the stress along the delamination front, enabling accurate evaluation of the crack growth rate. The methodology is applied here in conjunction with the cohesive zone model technique to evaluate the post-buckling fatigue behavior of a composite single-stringer specimen with an initial delamination. Comparisons with experimental data validate the predictive capabilities of the proposed approach. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Fatigue crack growth curve.</p>
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<p>Applied load ratio and local stress ratio in two locations along the delamination front.</p>
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<p>Min–Max Load Approach.</p>
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<p>Constitutive response for traction–separation cohesive elements.</p>
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<p>Implementation of the fatigue delamination model in the ABAQUS UMAT subroutine.</p>
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<p>SSCS geometry (dimensions in mm).</p>
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<p>FE model and boundary conditions.</p>
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<p>Geometrical imperfection: (<b>a</b>) measured with DIC; (<b>b</b>) initial imperfection in the FE model.</p>
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<p>Comparison between numerical and experimental quasi-static load-displacement curves.</p>
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<p>Numerical out-of-plane displacements and delamination front and size: (<b>a</b>) 18.7 kN; (<b>b</b>) 25 kN; (<b>c</b>) 27.4 kN (<b>d</b>) 33 kN. DIC images and C-scan at: (<b>e</b>) 20.0 kN; (<b>f</b>) 26.5 kN; (<b>g</b>) 30.0 kN; (<b>h</b>) 34.5 kN.</p>
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<p>FE models using the “Min–Max Load Approach” for the SSC specimen.</p>
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<p>Min–Max Load Approach out-of-plane displacements and damage propagation at: (<b>a</b>) first cycle; (<b>b</b>) 590 cycles; (<b>c</b>) 990 cycles. DIC and C-scan at: (<b>d</b>) first cycle; (<b>e</b>) 7000 cycles; (<b>f</b>) 50,000 cycles.</p>
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<p>Numerical out-of-plane displacements at: (<b>a</b>) 29.2 kN and (<b>b</b>) 2.92 kN; DIC images at: (<b>c</b>) 29.2 kN and (<b>d</b>) 2.92 kN. (<span class="html-italic">R<sub>Applied</sub></span> = 0.1).</p>
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<p>Numerical out-of-plane displacements at: (<b>a</b>) 29.2 kN and (<b>b</b>) 14.6 kN; DIC images at: (<b>c</b>) 29.2 kN and (<b>d</b>) 14.6 kN (<span class="html-italic">R<sub>Applied</sub></span> = 0.5).</p>
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<p>Local stress ratio for an applied (external) load ratio of: (<b>a</b>) 0.1; (<b>b</b>) 0.5.</p>
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16 pages, 3571 KiB  
Article
Numerical Investigation on the Capability of Modeling Approaches for Composite Cylinders under Low-Velocity Impact Loading
by Shiva Rezaei Akbarieh, Dayou Ma, Claudio Sbarufatti and Andrea Manes
J. Compos. Sci. 2024, 8(4), 141; https://doi.org/10.3390/jcs8040141 - 10 Apr 2024
Cited by 1 | Viewed by 1512
Abstract
Composite pressure vessels can be exposed to extreme loadings, for instance, impact loading, during manufacturing, maintenance, or their service lifetime. These kinds of loadings may provoke both visible and invisible levels of damage, e.g., fiber breakage matrix cracks and delamination and eventually may [...] Read more.
Composite pressure vessels can be exposed to extreme loadings, for instance, impact loading, during manufacturing, maintenance, or their service lifetime. These kinds of loadings may provoke both visible and invisible levels of damage, e.g., fiber breakage matrix cracks and delamination and eventually may lead to catastrophic failures. Thus, the quantification and evaluation of such damages are of great importance. Considering the cost of relevant full-scale experiments, a numerical model can be a powerful tool for such a kind of study. This paper aims to provide a numerical study to investigate the capability of different modeling methods to predict delamination in composite vessels. In this study, various numerical modeling aspects, such as element types (solid and shell elements) and material parameters (such as interface properties), were considered to investigate delamination in a composite pressure vessel under low-velocity impact loading. Specifically, solid elements were used to model each layer of the composite pressure vessel, while, in another model, shell elements with composite layup were considered. Compared with the available experimental data from low-velocity impact tests described in the literature, the capability of these two models to predict both mechanical responses and failure phenomena is shown. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Numerical model generated for the impact loading on the composite cylinder: (<b>a</b>) the model with solid elements; (<b>b</b>) the model with shell elements.</p>
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<p>The numerical model for the composite cylinder with various mesh sizes defined in the numerical model: (<b>a</b>) <math display="inline"><semantics> <mrow> <mn>1</mn> <mo>×</mo> <mn>1</mn> <mo> </mo> <mi mathvariant="normal">m</mi> <msup> <mrow> <mi mathvariant="normal">m</mi> </mrow> <mrow> <mn>2</mn> </mrow> </msup> </mrow> </semantics></math>; (<b>b</b>) <math display="inline"><semantics> <mrow> <mn>2</mn> <mo>×</mo> <mn>2</mn> <mo> </mo> <mi mathvariant="normal">m</mi> <msup> <mrow> <mi mathvariant="normal">m</mi> </mrow> <mrow> <mn>2</mn> </mrow> </msup> </mrow> </semantics></math>; (<b>c</b>) <math display="inline"><semantics> <mrow> <mn>3</mn> <mo>×</mo> <mn>3</mn> <mo> </mo> <mi mathvariant="normal">m</mi> <msup> <mrow> <mi mathvariant="normal">m</mi> </mrow> <mrow> <mn>2</mn> </mrow> </msup> </mrow> </semantics></math>.</p>
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<p>Traction–separation curves of (<b>a</b>) tiebreak behavior; (<b>b</b>) linear cohesive behavior; (<b>c</b>) non-linear cohesive behavior.</p>
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<p>Maximum strain and calculation time for the model with three different mesh sizes (columns 1–3). Data from experiments are shown in column 4.</p>
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<p>(<b>a</b>) The delamination area marked in red obtained in the numerical model with three different mesh sizes; (<b>b</b>) the delamination area obtained from experiment [<a href="#B40-jcs-08-00141" class="html-bibr">40</a>].</p>
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<p>Delamination area in different mesh size.</p>
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<p>Effect of three different mesh sizes in different element types on the size of the predicted delamination area marked in red. Scale bar as indicated.</p>
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<p>The delamination area after impact loading. (<b>a</b>) The delamination area (marked in red) obtained in the numerical model with the three different interface properties: typical tiebreak, linear cohesive model, and non-linear cohesive model. (<b>b</b>) The experimentally obtained delamination area [<a href="#B40-jcs-08-00141" class="html-bibr">40</a>].</p>
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<p>The delamination area marked in red obtained from the numerical model with two different element types: solid element and thick-shell element.</p>
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<p>Strain–time curves for numerical analysis using two different elements (solid elements with mesh size of 2 × 2 mm<sup>2</sup> and tiebreak model for the interface) marked in blue and shell elements (marked in green) and experimental results (marked in orange).</p>
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22 pages, 11714 KiB  
Article
Dynamic Behavior and Permanent Indentation in S2-Glass Woven Fabric Reinforced Polymer Composites under Impact: Experimentation and High-Fidelity Modeling
by Mohammad Rezasefat, Yogesh Kumar, Amanda Albertin Xavier da Silva, Sandro Campos Amico, James David Hogan and Andrea Manes
J. Compos. Sci. 2024, 8(4), 138; https://doi.org/10.3390/jcs8040138 - 9 Apr 2024
Viewed by 1506
Abstract
This paper studies the behavior of S2-glass woven fabric reinforced polymer composite under low-velocity impact at 18–110 J energy. A macro-homogeneous finite element model for the prediction of their response is implemented, considering the non-linear material behavior and intralaminar and interlaminar failure modes [...] Read more.
This paper studies the behavior of S2-glass woven fabric reinforced polymer composite under low-velocity impact at 18–110 J energy. A macro-homogeneous finite element model for the prediction of their response is implemented, considering the non-linear material behavior and intralaminar and interlaminar failure modes for the prediction of impact damage. The model accurately predicted the permanent indentation caused by impact. By applying the Ramberg-Osgood formulation, different initial stiffness values are examined to assess the post-impact unloading response. This approach reveals the significant role of initial stiffness in inelastic strain accumulation and its consequent effect on permanent indentation depth. A higher initial stiffness correlates with increased inelastic strain, influencing the impactor rebound and resulting in greater permanent indentation. By accurately predicting permanent indentation, and damage accumulation for different impact energies, this study contributes to a better understanding of the impact behavior of composite materials, thereby promoting their wider application. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Nonlinear material stress-strain behavior and post-damage softening (loading and unloading are indicated with the red arrows).</p>
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<p>Flowchart of the VUMAT or user-defined model for the material.</p>
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<p>3D finite element model of the laminate, clamping fixture, and hemispherical impactor.</p>
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<p>Experimental and numerical (from the Ramberg–Osgood formulation) stress-strain curves for the S2-glass woven fabric reinforced polymer composites.</p>
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<p>Force-time (<b>a</b>), force-displacement (<b>b</b>), energy-time (<b>c</b>), curves obtained for low-velocity impacts at different energy levels.</p>
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<p>Experimentally assessed damaged areas for different impact energies.</p>
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<p>Assessed contribution of each failure mode to the total damage of the specimen.</p>
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<p>Variation in experimental ratio of energy and total damaged area with impact energy.</p>
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<p>Experimental and numerical impact force/energy-time curves obtained for impacts at: (<b>a</b>) 18.4 J, (<b>b</b>) 27.8 J, (<b>c</b>) 44.8 J, and (<b>d</b>) 59.2 J.</p>
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<p>Experimental and numerical force-displacement curves for impacts at: (<b>a</b>) 18.4 J, (<b>b</b>) 27.8 J, (<b>c</b>) 44.8 J, and (<b>d</b>) 59.2 J.</p>
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<p>Normal and shear contact forces contribution for impact energies of: (<b>a</b>) 109.7 J, (<b>b</b>) 18.4 J.</p>
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<p>Mesh sensitivity results for: (<b>a</b>) dissipated energy and computational time, and (<b>b</b>) interlaminar and interlaminar damage predictions.</p>
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<p>Contour plots at different simulation times for the 109.7 J impact.</p>
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<p>Comparison of experimental and numerical damage morphology for impact energies of: (<b>a</b>) 27.8 J, (<b>b</b>) 44.8 J, (<b>c</b>) 71.3 J (the dashed red lines indicate the extent of damage through the thickness of the laminate).</p>
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<p>Prediction of permanent indentation—Displacement-time curves for models with different initial stiffness, with a zoomed view of the curves.</p>
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<p>(<b>a</b>) The effect of initial stiffness on permanent indentation (impact energy: 18.4 J), and (<b>b</b>) experimental and numerical permanent indentation data for different impact energies.</p>
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<p>(<b>a</b>) The effect of initial stiffness on permanent indentation (impact energy: 18.4 J), and (<b>b</b>) experimental and numerical permanent indentation data for different impact energies.</p>
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<p>Contour plots of permanent indentation for different initial modulus values.</p>
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13 pages, 2189 KiB  
Article
Mechanical and Thermal Properties of the Hf–Si System: First-Principles Calculations
by Panxin Huang, Guifang Han, Huan Liu, Weibin Zhang, Kexue Peng, Jianzhang Li, Weili Wang and Jingde Zhang
J. Compos. Sci. 2024, 8(4), 129; https://doi.org/10.3390/jcs8040129 - 2 Apr 2024
Viewed by 1512
Abstract
The relatively low melting point of a traditional Si bonding layer limits the upper servicing temperature of environmental barrier coatings (EBC). To explore suitable high temperature bonding layers and expedite the development of EBC, first-principles calculation was used to evaluate the mechanical properties [...] Read more.
The relatively low melting point of a traditional Si bonding layer limits the upper servicing temperature of environmental barrier coatings (EBC). To explore suitable high temperature bonding layers and expedite the development of EBC, first-principles calculation was used to evaluate the mechanical properties and thermal conductivity of HfSi2, HfSi, Hf5Si4, Hf3Si2, and Hf2Si with much higher melting points than that of Si. Among them, HfSi2 has the lowest modulus capable of good modulus matching with SiC substrate. In addition, these Hf-Si compounds have much lower high temperature thermal conductivity with Hf2Si being the lowest of 0.63 W m−1 K−1, which is only half of Si, capable of improved heat insulation. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Crystal structures of the Hf-Si system: (<b>a</b>) Si, (<b>b</b>) HfSi<sub>2</sub>, (<b>c</b>) HfSi, (<b>d</b>) Hf<sub>3</sub>Si<sub>2</sub>, (<b>e</b>) Hf<sub>2</sub>Si, (<b>f</b>) Hf<sub>5</sub>Si<sub>4</sub> (the blue represented Si atoms and the brown represented Hf atoms).</p>
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<p>Relative errors of lattice constants of the Hf-Si system.</p>
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<p>(<b>a</b>) Surface contour of direction-dependent Young’s modulus of Si and (<b>b</b>) its planar projections on (100), (010), and (001) crystallographic planes.</p>
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<p>Surface contour of direction-dependent Young’s modulus of (<b>a</b>) HfSi<sub>2</sub>, (<b>b</b>) HfSi, (<b>c</b>) Hf<sub>5</sub>Si<sub>4</sub>, (<b>d</b>) Hf<sub>3</sub>Si<sub>2</sub>, (<b>e</b>) Hf<sub>2</sub>Si and (<b>a<sub>1</sub></b>–<b>e<sub>1</sub></b>) planar projections on (100), (010), and (001) crystallographic planes.</p>
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<p>Temperature dependence of thermal conductivity of Si and HfSi<sub>2</sub>. The minimum thermal conductivity (dash line) was also shown.</p>
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20 pages, 17545 KiB  
Article
Impact Characteristics and Repair Approaches of Distinct Bio-Based Matrix Composites: A Comparative Analysis
by Bharath Ravindran, Timotheos Agathocleous, Beate Oswald-Tranta, Ewald Fauster and Michael Feuchter
J. Compos. Sci. 2024, 8(4), 126; https://doi.org/10.3390/jcs8040126 - 29 Mar 2024
Cited by 1 | Viewed by 1754
Abstract
Increasing global concerns regarding environmental issues have driven significant advancements in the development of bio-based fiber reinforced polymer composites. Despite extensive research on bio-composites, there remains a noticeable gap in studies specifically addressing the challenges of repairing bio-composites for circular economy adoption. Traditional [...] Read more.
Increasing global concerns regarding environmental issues have driven significant advancements in the development of bio-based fiber reinforced polymer composites. Despite extensive research on bio-composites, there remains a noticeable gap in studies specifically addressing the challenges of repairing bio-composites for circular economy adoption. Traditional repair techniques for impacted composites, such as patching or scarf methods, are not only time-consuming but also require highly skilled personnel. This paper aims to highlight cost-effective repair strategies for the restoration of damaged composites, featuring flax fiber as the primary reinforcement material and distinct matrix systems, namely bio-based epoxy and bio-based vitrimer matrix. Glass fiber was used as a secondary material to validate the bio-based vitrimer matrix. The damage caused specifically by low impact is detrimental to the structural integrity of the composites. Therefore, the impact resistance of the two composite materials is evaluated using instrumented drop tower tests at various energy levels, while thermography observations are employed to assess damage evolution. Two distinct repair approaches were studied: the resin infiltration repair method, employing bio-based epoxy, and the reconsolidation (self-healing) repair method, utilizing the bio-based vitrimer matrix. The efficiency of these repair methods was assessed through active thermography and compression after impact tests. The repair outcomes demonstrate successful restoration and the maintenance of ultimate strength at an efficiency of 90% for the re-infiltration repair method and 92% for the reconsolidation repair method. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Chemical structure of epoxidized linseed oil [<a href="#B44-jcs-08-00126" class="html-bibr">44</a>], glutaric anhydride [<a href="#B45-jcs-08-00126" class="html-bibr">45</a>] and TBD [<a href="#B46-jcs-08-00126" class="html-bibr">46</a>].</p>
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<p>Schematic of VARI setup.</p>
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<p>Schematic representation outlining the impact testing.</p>
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<p>Schematic representation of repair activities.</p>
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<p>Drop tower impact test.</p>
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<p>Active flash thermography setup.</p>
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<p>Impacted specimens drilling: drill equipment (<b>left</b>) and drilled impacted specimen (<b>right</b>).</p>
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<p>Schematic of resin reinfiltration repair setup.</p>
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<p>Resin reinfiltration repair approach: repair setup after injection (<b>left</b>) and oven curing (<b>right</b>).</p>
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<p>Schematic of reconsolidation repair setup: impacted specimen is placed on press at 160 °C (<b>left</b>) and reconsolidated (healed) after four hours (<b>right</b>).</p>
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<p>Reconsolidation repair approach: impacted specimen between gauge tape bundles (<b>left</b>) and press with heating mold (<b>right</b>).</p>
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<p>Compression after impact testing.</p>
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<p>Impact characteristic at impact energy level 10 J: force vs. time (<b>left</b>) and force vs. displacement (<b>right</b>).</p>
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<p>Impact characteristics at varied energy levels: peak force (<b>left</b>), displacement (<b>middle</b>) and absorbed energy (<b>right</b>).</p>
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<p>Front, rear and thermography image of FBEC impacted specimen.</p>
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<p>Front, rear and thermography image of FBVC impacted specimen.</p>
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<p>Reinfiltration repair process: after 1 min (<b>left</b>), after 5 min (<b>middle</b>) and after 10 min (<b>right</b>).</p>
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<p>Thermography sequence of FBEC specimens: undamaged (<b>left</b>), damaged (<b>middle</b>) and repaired (<b>right</b>).</p>
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<p>Comparison before and after repair via reinfiltration.</p>
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<p>Load–displacement graph of specimens from CAI testing (<b>left</b>) and CAI compression strength of undamaged, damaged and repaired FBEC specimens (<b>right</b>).</p>
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<p>Thermography sequence of FBVC specimens: undamaged (<b>left</b>), damaged (<b>middle</b>) and repaired (<b>right</b>).</p>
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<p>Comparison before and after repair via reconsolidation.</p>
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<p>Load–displacement graph of specimens from CAI testing (<b>left</b>) and CAI compression strength of undamaged, damaged and repaired FBVC specimens (<b>right</b>).</p>
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<p>Comparison of GBVC specimens: before reconsolidation (<b>left</b>) and after reconsolidation (<b>right</b>).</p>
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<p>Load–displacement graph of specimens from CAI testing (<b>left</b>) and CAI compression strength of undamaged, damaged and repaired GBVC specimens (<b>right</b>).</p>
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28 pages, 26981 KiB  
Article
Micro- and Macro-Scale Topology Optimization of Multi-Material Functionally Graded Lattice Structures
by Jerónimo Santos, Abdolrasoul Sohouli and Afzal Suleman
J. Compos. Sci. 2024, 8(4), 124; https://doi.org/10.3390/jcs8040124 - 28 Mar 2024
Cited by 2 | Viewed by 1884
Abstract
Lattice structures are becoming an increasingly attractive design approach for the most diverse engineering applications. This increase in popularity is mainly due to their high specific strength and stiffness, considerable heat dissipation, and relatively light weight, among many other advantages. Additive manufacturing techniques [...] Read more.
Lattice structures are becoming an increasingly attractive design approach for the most diverse engineering applications. This increase in popularity is mainly due to their high specific strength and stiffness, considerable heat dissipation, and relatively light weight, among many other advantages. Additive manufacturing techniques have made it possible to achieve greater flexibility and resolution, enabling more complex and better-performing lattice structures. Unrestricted material unit cell designs are often associated with high computational power and connectivity problems, and highly restricted lattice unit cell designs may not reach the optimal desired properties despite their lower computational cost. This work focuses on increasing the flexibility of a restricted unit cell design while achieving a lower computational cost. It is based on a two-scale concurrent optimization of the lattice structure, which involves simultaneously optimizing the topology at both the macro- and micro-scales to achieve an optimal topology. To ensure a continuous optimization approach, surrogate models are used to define material and geometrical properties. The elasticity tensors for a lattice unit cell are obtained using an energy-based homogenization method combined with voxelization. A multi-variable parameterization of the material unit cell is defined to allow for the synthesis of functionally graded lattice structures. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Cross + Diamond geometry. (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math>. (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math>. (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math>.</p>
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<p>Cube + Inner Diagonal Cross geometry. (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math>. (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math>. (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math>.</p>
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<p>Diagonal Cross + Diamond geometry. (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math>. (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math>. (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math>.</p>
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<p>Diagonal Cross + Inner Cage geometry. (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math>. (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math>. (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math>.</p>
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<p>Diagonal Cross + Inner cross geometry. (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math>. (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math>. (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math>.</p>
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<p>Diagonal Cross + Inner Diagonal Cross geometry. (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math>. (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math>. (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math>.</p>
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<p>Case studies [<a href="#B30-jcs-08-00124" class="html-bibr">30</a>]. (<b>a</b>) Cantilever case study. (<b>b</b>) Messerchimitt–Bolkow–Blohm (MBB) case study. (<b>c</b>) Hook case study. (<b>d</b>) Wheel case study.</p>
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<p>Cantilever case study: Cross + Diamond geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Cross + Diamond geometry applied to the Cantilever case study.</p>
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<p>Cantilever case study: Cube + Inner diagonal cross geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Cube + Inner diagonal cross geometry applied to the Cantilever case study.</p>
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<p>Cantilever case study: Diagonal cross + Diamond geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Diamond geometry applied to the Cantilever case study.</p>
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<p>Cantilever case study: Diagonal cross + Inner cage geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Inner cage geometry applied to the Cantilever case study.</p>
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<p>Cantilever case study: Diagonal cross + Inner cross geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Inner cross geometry applied to the Cantilever case study.</p>
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<p>Cantilever case study: Diagonal cross + Inner diagonal cross geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Inner diagonal cross geometry applied to the Cantilever case study.</p>
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<p>MBB case study: Cross + Diamond geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Cross + Diamond geometry applied to the MBB case study.</p>
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<p>MBB case study: Cube + Inner diagonal cross geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Cube + Inner diagonal cross geometry applied to the MBB case study.</p>
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<p>MBB case study: Diagonal cross + Diamond geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Diamond geometry applied to the MBB case study.</p>
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<p>MBB case study: Diagonal cross + Inner cage geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Inner cage geometry applied to the MBB case study.</p>
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<p>MBB case study: Diagonal cross + Inner cross geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Inner cross geometry applied to the MBB case study.</p>
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<p>MBB case study: Diagonal cross + Inner diagonal cross geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Inner diagonal cross geometry applied to the MBB case study.</p>
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<p>Hook case study: Cross + Diamond geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Cross + Diamond geometry applied to the Hook case study.</p>
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<p>Hook case study: Cube + Inner diagonal cross geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Cube + Inner diagonal cross geometry applied to the Hook case study.</p>
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<p>Hook case study: Diagonal cross + Diamond geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Diamond geometry applied to the Hook case study.</p>
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<p>Hook case study: Diagonal cross + Inner cage geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Inner cage geometry applied to the Hook case study.</p>
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<p>Hook case study: Diagonal cross + Inner cross geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Inner cross geometry applied to the Hook case study.</p>
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<p>Hook case study: Diagonal cross + Inner diagonal cross geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Inner diagonal cross geometry applied to the Hook case study.</p>
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<p>Wheel case study: Cross + Diamond geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Cross + Diamond geometry applied to the Wheel case study.</p>
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<p>Wheel case study: Cube + Inner diagonal cross geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Cube + Inner diagonal cross geometry applied to the Wheel case study.</p>
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<p>Wheel case study: Diagonal cross + Diamond geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Diamond geometry applied to the Wheel case study.</p>
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<p>Wheel case study: Diagonal cross + Inner cage geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Inner cage geometry applied to the Wheel case study.</p>
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<p>Wheel case study: Diagonal cross + Inner cross geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Inner cross geometry applied to the Wheel case study.</p>
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<p>Wheel case study: Diagonal cross + Inner diagonal cross geometry. (<b>a</b>) Relative density distribution—material 1 in blue, material 2 in red. (<b>b</b>) Aspect ratio distribution. (<b>c</b>) Render: Diagonal cross + Inner diagonal cross geometry applied to the Wheel case study.</p>
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<p>Compliance comparison between geometries. (<b>a</b>) Compliance comparison between TO final results for 3 geometries, each geometry with <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> </semantics></math> varying from 0 to 1. (<b>b</b>) Compliance comparison between TO final results for 3 geometries, each with <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> </semantics></math> varying from 0 to 1. (<b>c</b>) Compliance comparison between TO final results for 3 geometries, each with <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> </semantics></math> varying from 0 to 1. (<b>d</b>) Compliance comparison between TO final results for 3 geometries, each with <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> </semantics></math> varying from 0 to 1.</p>
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<p>Compliance comparison between geometries. (<b>a</b>) Compliance comparison between TO final results for 3 geometries, each with <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> </semantics></math> varying from 0 to 1. (<b>b</b>) Compliance comparison between TO final results for 3 geometries, each with <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> </semantics></math> varying from 0 to 1. (<b>c</b>) Compliance comparison between TO final results for 3 geometries, each with <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> </semantics></math> varying from 0 to 1. (<b>d</b>) Compliance comparison between TO final results for 3 geometries, each with <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <mrow> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math> or <math display="inline"><semantics> <msub> <mi>ρ</mi> <mrow> <mi>e</mi> <mi>x</mi> <mi>t</mi> </mrow> </msub> </semantics></math> varying from 0 to 1.</p>
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<p>Render: Cross + Diamond geometry applied to the Cantilever case study.</p>
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<p>Render: Cube + Inner diagonal cross geometry applied to the Cantilever case study.</p>
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<p>Render: Diagonal cross + Diamond geometry applied to the Cantilever case study.</p>
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<p>Render: Diagonal cross + Inner cage geometry applied to the Cantilever case study.</p>
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<p>Render: Diagonal cross + Inner cross geometry applied to the Cantilever case study.</p>
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<p>Render: Diagonal cross + Inner diagonal cross geometry applied to the Cantilever case study.</p>
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<p>Render: Cross + Diamond geometry applied to the MBB case study.</p>
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<p>Render: Cube + Inner diagonal cross geometry applied to the MBB case study.</p>
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<p>Render: Diagonal cross + Diamond geometry applied to the MBB case study.</p>
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<p>Render: Diagonal cross + Inner cage geometry applied to the MBB case study.</p>
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<p>Render: Diagonal cross + Inner cross geometry applied to the MBB case study.</p>
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<p>Render: Diagonal cross + Inner diagonal cross geometry applied to the MBB case study.</p>
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<p>Render: Cross + Diamond geometry applied to the Hook case study.</p>
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<p>Render: Cube + Inner diagonal cross geometry applied to the Hook case study.</p>
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<p>Render: Diagonal cross + Diamond geometry applied to the Hook case study.</p>
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<p>Render: Diagonal cross + Inner cage geometry applied to the Hook case study.</p>
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<p>Render: Diagonal cross + Inner cross geometry applied to the Hook case study.</p>
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<p>Render: Diagonal cross + Inner diagonal cross geometry applied to the Hook case study.</p>
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<p>Render: Cross + Diamond geometry applied to the Wheel case study.</p>
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<p>Render: Cube + Inner diagonal cross geometry applied to the Wheel case study.</p>
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<p>Render: Diagonal cross + Diamond geometry applied to the Wheel case study.</p>
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<p>Render: Diagonal cross + Inner cage geometry applied to the Wheel case study.</p>
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<p>Render: Diagonal cross + Inner cross geometry applied to the Wheel case study.</p>
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<p>Render: Diagonal cross + Inner diagonal cross geometry applied to the Wheel case study.</p>
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17 pages, 12134 KiB  
Article
Mitigating Crack Propagation in Hybrid Composites: An Experimental and Computational Study
by Suma Ayyagari and Marwan Al-Haik
J. Compos. Sci. 2024, 8(4), 122; https://doi.org/10.3390/jcs8040122 - 27 Mar 2024
Viewed by 1680
Abstract
The exceptional properties of carbon nanotubes (CNTs) make them ideal nanofillers for various composite materials. In carbon fiber-reinforced polymer (CFRP) composites. CNTs can be grown on the carbon fiber surface to act as a third interface between the fiber and the matrix. However, [...] Read more.
The exceptional properties of carbon nanotubes (CNTs) make them ideal nanofillers for various composite materials. In carbon fiber-reinforced polymer (CFRP) composites. CNTs can be grown on the carbon fiber surface to act as a third interface between the fiber and the matrix. However, it was established that the uncontrolled random growth of CNTs could exacerbate delamination in composite structures. Thick nanofiller films could hinder the epoxy from seeping into the carbon fiber, resulting in insufficient interlaminar strength. Hence, the density and distribution of nanofillers play a crucial role in determining the hybrid composite fracture mechanisms. In this investigation, CNTs were grown using the low-temperature technique into specific patterns over carbon fibers to discern their derived composites’ fracture properties. The composite fracture energy release was probed using a double cantilever beam (DCB) test setup and digital image correlation (DIC) to monitor interlaminar crack propagation. A standard finite element simulation model based on the cohesive zone method (CZM) was also utilized to delineate fracture behaviors of the various composite configurations. Results conclude that a coarser pattern of CNT growth enhances resistance to crack propagation, thus improving the interlaminar fracture toughness of a composite structure. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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Figure 1

Figure 1
<p>Schematic illustration of crack (red curve) propagation in a laminate of (<b>a</b>) carbon fiber with uniformly grown CNTs and (<b>b</b>) carbon fiber with pattern-grown CNTs.</p>
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<p>SEM micrographs of CNTs grown on silicon wafers (<b>a</b>) CNTs grown utilizing a 105 μm perforated mesh pattern (inset figure scale bar 400 μm), and (<b>b</b>) Uniform CNTs growth pattern.</p>
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<p>SEM micrographs (at different magnifications) of CNTs grown on the carbon fiber surface using the GSD process.</p>
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<p>Composite lamination and testing coupon illustration.</p>
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<p>The DCB test setup shows a crack opening of a composite test coupon acquired by the DIC system.</p>
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<p>(<b>a</b>) 3D model of a DCB test specimen with boundary conditions and input loading, coarsely meshed in the pre-cracked region and finely meshed in the crack propagation region. (<b>b</b>) The model after crack propagation.</p>
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<p>The model was built in ANSYS for delamination after the CZM analysis.</p>
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<p>Representative load vs. load point displacement curves for the different composite configurations.</p>
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<p>Delamination crack length vs. load for the different composite configurations. Dotted lines represent data regression.</p>
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<p>Delamination crack length vs. load point displacement for the different composite configurations.</p>
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<p>Interlaminar fracture toughness comparison for all composite configurations. Dotted lines represent data regression.</p>
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<p>SEM micrographs of the DCB sample damaged surfaces for composites based on (<b>a</b>) desized carbon fibers, (<b>b</b>) carbon fibers with uniform growth of CNTs, and (<b>c</b>) carbon fibers with 105 μm pattern grown CNTs.</p>
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<p>FEM model prediction of the load vs. load point displacement using CZM for the different composite configurations.</p>
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<p>Prediction of the delamination crack length vs. load using the CZM model for the different composite configurations.</p>
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<p>Interlaminar fracture toughness comparison for the different composite configurations using the CZM model.</p>
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<p>Interlaminar fracture toughness of the different composite configurations using DCB experiments and the CZM model.</p>
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13 pages, 4060 KiB  
Article
Optimization of a Tapered Specimen Geometry for Short-Term Dynamic Tensile Testing of Continuous Fiber Reinforced Thermoplastics
by Florian Mischo and Sebastian Schmeer
J. Compos. Sci. 2024, 8(3), 93; https://doi.org/10.3390/jcs8030093 - 3 Mar 2024
Cited by 1 | Viewed by 1529
Abstract
Continuous fiber reinforced thermoplastics (cFRTP) are one of the most promising lightweight materials. For their use in structural components, reproducible and comparable material values have to be evaluated, especially at high strain rates. Due to their high stiffness and outstanding strength properties, the [...] Read more.
Continuous fiber reinforced thermoplastics (cFRTP) are one of the most promising lightweight materials. For their use in structural components, reproducible and comparable material values have to be evaluated, especially at high strain rates. Due to their high stiffness and outstanding strength properties, the evaluation of the material behavior at high strain rates is complex. In the presented work, a new tensile specimen geometry for strain rate testing is virtually optimized using a metamodel approach with an artificial neural network. The final specimen design is experimentally validated and compared with rectangular specimen results for a carbon fiber reinforced polycarbonate (CF-PC). The optimized specimen geometry leads to 100% valid test results in experimental validation of cross-ply laminates and reaches 9% higher tensile strength values than the rectangle geometry with applied end tabs at a strain rate of 40 s−1. Through the optimization, comparable material parameters can be efficiently generated for a successful cFRTP strain rate characterization. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Network of neurons <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>z</mi> </mrow> <mrow> <mi>i</mi> </mrow> </msub> </mrow> </semantics></math> of a single layer neural network.</p>
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<p>Quarter-model representation of the tapered tensile specimen to optimize.</p>
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<p>Optimization flow chart of the tapered tensile specimen geometry.</p>
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<p>Three-dimensional visualization of the metamodel (<b>e</b>); Two-dimensional cutting planes (<b>a</b>–<b>d</b>) through the global minimum of Max(<math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="sans-serif">τ</mi> </mrow> <mrow> <mn>12</mn> </mrow> </msub> </mrow> </semantics></math>) of the five-dimensional metamodel.</p>
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<p>Stress exposure progression at the specimen’s edge of the optimized specimen geometry in CF-PC-UD laminate.</p>
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<p>Final specimen design for short-term dynamic tensile testing of cFRTP.</p>
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<p>Tensile results (mean value curves) of optimized geometries (ZDG) and rectangular reference specimens (ISO) for CF-PC-UD at a quasi-static (QS) test speed and at 4 m s<sup>−1</sup> (DYN).</p>
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<p>Tensile results (mean value curves) of optimized geometries (ZDG) and rectangular reference specimens (ISO) for CF-PC-KV at a quasi-static (QS) test speed and at 4 m s<sup>−1</sup> (DYN).</p>
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<p>Failure pattern of tested CF-PC-KV specimen batches: ZDG (<b>left</b>) and ISO (<b>right</b>) at test speeds QS (<b>first row</b>) and DYN (<b>second row</b>); dotted lines indicate first tensile failure; shaded areas indicate specimen slipping in clamping area.</p>
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17 pages, 3297 KiB  
Article
Experimental Comparative Analysis of the Through-Thickness and In-Plane Compression Moduli of Unidirectional CFRP Laminates
by Raffael Bogenfeld
J. Compos. Sci. 2024, 8(2), 76; https://doi.org/10.3390/jcs8020076 - 13 Feb 2024
Cited by 1 | Viewed by 1843
Abstract
This study explores the experimental characterization of the through-thickness compression properties in unidirectional laminates using cube compression tests. Cubical specimens, each with an edge length of 10 mm, were symmetrically outfitted with biaxial strain gauges and subjected to a compression test. While similar [...] Read more.
This study explores the experimental characterization of the through-thickness compression properties in unidirectional laminates using cube compression tests. Cubical specimens, each with an edge length of 10 mm, were symmetrically outfitted with biaxial strain gauges and subjected to a compression test. While similar methodologies exist in the literature, this work primarily addresses the potential biases inherent in the testing procedure and their mitigation. The influence of friction-induced non-uniform deformation behavior is compensated through a scaling of the stiffness measurements using finite element (FE) analysis results. This scaling significantly enhances the accuracy of the resulting parameters of the experiments. The ultimate failure of the specimens, originating from stress concentrations at the edges, resulted in fracture angles ranging between 60° and 67°. Such fracture patterns, consistent with findings from other researchers, are attributed to shear stress induced by friction at the load introduction faces. The key findings of this research are the comparisons between the through-thickness modulus (E33c) and strength (X33c) and their in-plane counterparts (E22c and X22c). The results indicate deteriorations of E33c and X33c from E22c and X22c by margins of 5% and 7%, respectively. Furthermore, the results for E22c and X22c were compared with the results obtained through a standard test, revealing a 12% enhancement in strength X22c and 4% underestimated stiffness E22c in the cube compression test. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>The experimental set-up for the compression test as schematics (<b>left</b>) and as an actual photo (<b>right</b>).</p>
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<p>Strain gauges configurations for the cubical specimens for the 3-direction test and the 2-direction test.</p>
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<p>A set of 8 specimens equipped with strain gauges.</p>
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<p>(<b>a</b>) Explicit FE model of the specimen and the hardened steel plates with penalty contact between the bodies, including the boundary condition model features. (<b>b</b>) Representation to scale of the strain gauge positions and sizes on the FE mesh (measuring grids illustrated in yellow).</p>
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<p>Strain results for the deformed cube under a compression load level of <math display="inline"><semantics> <mrow> <mn>6</mn> <mrow/> </mrow> </semantics></math> kN (visualization by SpectrumBaker [<a href="#B31-jcs-08-00076" class="html-bibr">31</a>]).</p>
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<p>Distribution of the calculated modulus <math display="inline"><semantics> <msub> <mi>E</mi> <mn>33</mn> </msub> </semantics></math> based on the local strain result <math display="inline"><semantics> <msub> <mi>ε</mi> <mn>33</mn> </msub> </semantics></math> of the FE analysis at a load level of <math display="inline"><semantics> <mrow> <mn>6</mn> <mrow/> </mrow> </semantics></math> kN (visualization by SpectrumBaker [<a href="#B31-jcs-08-00076" class="html-bibr">31</a>]). (<b>a</b>) <math display="inline"><semantics> <msub> <mi>E</mi> <mn>33</mn> </msub> </semantics></math> as measurable on the 23-face. (<b>b</b>) <math display="inline"><semantics> <msub> <mi>E</mi> <mn>33</mn> </msub> </semantics></math> as measurable on the 13-face.</p>
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<p>Distribution of the calculated Poisson’s ratios <math display="inline"><semantics> <msub> <mi>ν</mi> <mn>31</mn> </msub> </semantics></math> and <math display="inline"><semantics> <msub> <mi>ν</mi> <mn>32</mn> </msub> </semantics></math> based on the local strain results <math display="inline"><semantics> <msub> <mi>ε</mi> <mn>33</mn> </msub> </semantics></math>, <math display="inline"><semantics> <msub> <mi>ε</mi> <mn>11</mn> </msub> </semantics></math>, and <math display="inline"><semantics> <msub> <mi>ε</mi> <mn>22</mn> </msub> </semantics></math> of the FE analysis at a load level of <math display="inline"><semantics> <mrow> <mn>6</mn> <mrow/> </mrow> </semantics></math> kN (visualization by SpectrumBaker [<a href="#B31-jcs-08-00076" class="html-bibr">31</a>]): (<b>a</b>) locally measurable <math display="inline"><semantics> <msub> <mi>ν</mi> <mn>32</mn> </msub> </semantics></math> of the deformed cube under a compression load level of <math display="inline"><semantics> <mrow> <mn>6</mn> <mrow/> </mrow> </semantics></math> kN and (<b>b</b>) locally measurable <math display="inline"><semantics> <msub> <mi>ν</mi> <mn>31</mn> </msub> </semantics></math> of the deformed cube under a compression load level of <math display="inline"><semantics> <mrow> <mn>6</mn> <mrow/> </mrow> </semantics></math> kN.</p>
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<p>Raw strain vs. force measurements of the <math display="inline"><semantics> <msub> <mi>E</mi> <mn>33</mn> </msub> </semantics></math> tests. (<b>a</b>) Individual strains measured in the loading direction on both 13-planes. (<b>b</b>) Individual strains measured in the loading direction on both 23-planes.</p>
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<p>Strain vs. force plots from measurements of the <math display="inline"><semantics> <msub> <mi>E</mi> <mn>33</mn> </msub> </semantics></math> tests (<b>a</b>) Averaged strain <math display="inline"><semantics> <msub> <mi>ε</mi> <mn>33</mn> </msub> </semantics></math> from both opposing planes. (<b>b</b>) Strains <math display="inline"><semantics> <msub> <mi>ε</mi> <mn>11</mn> </msub> </semantics></math> and <math display="inline"><semantics> <msub> <mi>ε</mi> <mn>22</mn> </msub> </semantics></math> measured in the transverse direction.</p>
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<p>Results for the raw moduli <math display="inline"><semantics> <msub> <mi>E</mi> <mn>33</mn> </msub> </semantics></math> and <math display="inline"><semantics> <msub> <mi>E</mi> <mn>22</mn> </msub> </semantics></math> for strain gauge configuration (yz planes/xz planes). (<b>a</b>) Raw Young’s moduli. (<b>b</b>) Raw Poisson’s ratios.</p>
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<p>Results for the corrected moduli <math display="inline"><semantics> <msub> <mi>E</mi> <mn>33</mn> </msub> </semantics></math> and <math display="inline"><semantics> <msub> <mi>E</mi> <mn>22</mn> </msub> </semantics></math> for each configuration and the averaged values. (<b>a</b>) Young’s moduli. (<b>b</b>) Poisson’s ratio.</p>
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<p>Failure pattern view on the 23-plane of the tested specimens after ultimate failure.</p>
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<p>(<b>a</b>) Comparison of the fracture angle between the present study and the fractured specimens shown by Zhang et al. [<a href="#B21-jcs-08-00076" class="html-bibr">21</a>] and Kim et al. [<a href="#B22-jcs-08-00076" class="html-bibr">22</a>]. (<b>b</b>) Directions of the major principal stress at the loading faces of the specimen.</p>
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<p>Failure patterns of the specimens of the fiber direction tests.</p>
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14 pages, 9975 KiB  
Article
Development of a Novel Lightweight Utility Pole Using a New Hybrid Reinforced Composite—Part 2: Numerical Simulation and Design Procedure
by Qianjiang Wu and Farid Taheri
J. Compos. Sci. 2024, 8(2), 50; https://doi.org/10.3390/jcs8020050 - 30 Jan 2024
Cited by 1 | Viewed by 1690
Abstract
The first paper of this two-part series discussed the development of a novel lightweight 3D wood dowel-reinforced glass epoxy hybrid composite material (3DdrFRP) and its manufacturing procedures. It also experimentally compared the performance of scaled utility poles made from conventional 2D E-glass epoxy [...] Read more.
The first paper of this two-part series discussed the development of a novel lightweight 3D wood dowel-reinforced glass epoxy hybrid composite material (3DdrFRP) and its manufacturing procedures. It also experimentally compared the performance of scaled utility poles made from conventional 2D E-glass epoxy and 3DdrFRP materials. In the second part, the development of robust, efficient, and fairly accurate nonlinear finite element (FE) models is outlined. The models are calibrated based on experimental results and used to simulate the performance of equivalent 2D and 3D poles, proving the integrity of the numerical models. Additionally, a simplified analytical calculation method is developed for practicing engineers to evaluate the stiffness of 3D-DrFRP poles fairly accurately and quickly. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>(<b>a</b>) The dimensions of the 3D E-glass epoxy unit cell used in all numerical models; (<b>b</b>) a view of the actual flexural specimen.</p>
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<p>The quarter symmetry model of the flexural test specimens and the imposed boundary conditions.</p>
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<p>Comparison of the load–displacement responses of the flexural specimens and the numerically predicted results.</p>
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<p>Comparison of the post-failure damage on the actual specimen and the numerically predicted; (<b>a</b>,<b>b</b>) show the side view and (<b>c</b>,<b>d</b>) show the top view.</p>
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<p>Compression of the experimental and numerically predicted compressive failure modes of a 3DdrFRP specimen under compressive loading: (<b>a</b>) experimental front view, (<b>b</b>) numerical front view, (<b>c</b>) experimental side view; (<b>d</b>) numerical side view.</p>
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<p>(<b>a</b>) Illustration of boundary conditions accounting for the fixture; (<b>b</b>) mesh of the overlap region of the tapered poles.</p>
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<p>Comparison of the experimental and numerical load–deflection curves of the 2D poles at the tip and mid-height.</p>
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<p>Comparison of the variation in the experimental and numerically obtained results: (<b>a</b>) tensile and compressive strains; (<b>b</b>) hop strain, as a function of the applied tip displacement.</p>
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<p>(<b>a</b>) The fully restrained nodes on the inner surface of the pole; (<b>b</b>) the load ring attached to the pole using the contact algorithm.</p>
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<p>Comparison of the experimental and numerically predicted load–deflection curves.</p>
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<p>Comparison of experimental and FE strain–tip deflection curves for 3D poles.</p>
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<p>Local buckling model of the pole near the groundline on the compressive side of the pole. Note: Colors yellow, blue and green signify the cross-ply layers and pillars of the 3D fabric, and wood dowels, respectively.</p>
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<p>Comparison of the 2D and 3D poles.</p>
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12 pages, 5834 KiB  
Article
Characterization of Interlaminar Friction during the Forming Processes of High-Performance Thermoplastic Composites
by Daniel Campos, Pere Maimí and Alberto Martín
J. Compos. Sci. 2024, 8(2), 38; https://doi.org/10.3390/jcs8020038 - 23 Jan 2024
Cited by 1 | Viewed by 2053
Abstract
Friction is a pivotal factor influencing wrinkle formation in composite material shaping processes, particularly in novel thermoplastic composites like polyetheretherketone (PEEK) and low-melting polyaryletherketone (LM-PAEK) matrices reinforced with unidirectional carbon fibers. The aerospace sector lacks comprehensive data on the behavior of these materials [...] Read more.
Friction is a pivotal factor influencing wrinkle formation in composite material shaping processes, particularly in novel thermoplastic composites like polyetheretherketone (PEEK) and low-melting polyaryletherketone (LM-PAEK) matrices reinforced with unidirectional carbon fibers. The aerospace sector lacks comprehensive data on the behavior of these materials under forming conditions, motivating this study’s objective to characterize the interlaminar friction of such high-performance thermoplastic composites across diverse temperatures and forming parameters. Differential scanning calorimetry (DSC) and dynamic mechanical analysis (DMA) were employed to analyze the thermomechanical behaviors of PEEK and LM-PAEK. These data guided friction tests covering room-to-forming temperatures. Horizontal pull-out fixed-plies tests were conducted to determine the friction coefficient and shear stress dependency concerning temperature, pressure, and pulling rate. Below the melting point, both materials adhered to Coulomb’s law for friction behavior. However, above the melting temperature, PEEK’s friction decreased while LM-PAEK’s friction increased with rising temperatures. These findings highlight the distinct responses of these materials to temperature variations, pulling rates, and pressures, emphasizing the need for further research on friction characterization around glass transition and melting temperatures to enhance our understanding of this phenomenon. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>(<b>a</b>) Laminate over tool. (<b>b</b>) Upper radio wrinkles due to a wrong plies’ displacement. (<b>c</b>) Bookend effect due to a proper displacement of the plies.</p>
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<p>Scheme of the experimental rig devised to measure the friction coefficient.</p>
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<p>(<b>a</b>) DSC results of TC1225/T700 LM-PAEK. (<b>b</b>) DSC results of APC2/AS4 PEEK. In green first heating cycle. In gray second heating cycle.</p>
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<p>DMA results. The APC2/AS4 demonstrates higher energy storage while exhibiting lower depletion during phase transitions compared to the TC1225/T700.</p>
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<p>APC-2/AS4 friction test vs. temperature results (pulling rate 2 mm/s. normal force 60N). (<b>a</b>) Friction force vs. displacement. (<b>b</b>) Shear stress vs. pressure. (<b>c</b>) Friction coefficient vs. pressure.</p>
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<p>TC1225/T700 friction test vs. temperature results (pulling rate 2 mm/s. normal force 60N). (<b>a</b>) Friction force vs. displacement. (<b>b</b>) Shear stress vs. pressure. (<b>c</b>) Friction coefficient vs. pressure.</p>
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<p>Influence of temperature. T<sub>0</sub>: room temperature, T<sub>g−50</sub>: glass transition temperature −50 °C, T<sub>g+50</sub>: glass transition temperature +50 °C, T<sub>M, ONSET</sub>: temperature at the onset of the melting peak, T<sub>M, PEAK</sub>: temperature at the melting peak, T<sub>M, OFFSET</sub>: temperature at the melting peak offset, T<sub>P</sub>: processing temperature. Note: The dynamic friction of the coefficient corresponds to the measure at 20 mm of displacement.</p>
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<p>APC2/AS4 pulling rate dependency. (<b>a</b>) Shear stress vs. pressure for T = 20 °C and T = 400 °C. (<b>b</b>) Shear stress vs. pulling rate for T = 400 °C.</p>
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<p>TC1225/T700 pressure dependency.</p>
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20 pages, 10998 KiB  
Article
The Behavior of Banyan (B)/Banana (Ba) Fibers Reinforced Hybrid Composites Influenced by Chemical Treatment on Tensile, Bending and Water Absorption Behavior: An Experimental and FEA Investigation
by Prabhakar C. G, M Sreenivas Reddy, Shashanka Rajendrachari, Rayappa Shrinivas Mahale, V. Mahesh and Anup Pandith
J. Compos. Sci. 2024, 8(1), 31; https://doi.org/10.3390/jcs8010031 - 13 Jan 2024
Cited by 3 | Viewed by 2045
Abstract
Natural fiber-based composites are highly prioritized in present industries due to their properties and benefits over synthetic fibers. Due to their biodegradable nature, banyan and banana fibers were used for the present work. This paper deals with an experimental and FEA investigation of [...] Read more.
Natural fiber-based composites are highly prioritized in present industries due to their properties and benefits over synthetic fibers. Due to their biodegradable nature, banyan and banana fibers were used for the present work. This paper deals with an experimental and FEA investigation of the tensile and bending behavior of banyan (B) and banana (Ba)-reinforced composites with different volume fractions, such as 25B/25Ba, 30B/20Ba, and 35B/15Ba, with a 50% weight fraction of epoxy resin and different fiber orientations. The hybrid composites treated with a 5% NaOH solution have better results as compared to untreated hybrid composites, with a volume fraction of 30% banyan fibers and 20% banana fiber (30B/20Ba), giving greater tensile and flexural properties for both treated and untreated fiber composites when compared to other volume fraction composites at 0/0/0/0 orientation. The maximum tensile and bending strength was found in the 30B/20Ba volume fractions to be 63.37 MPa and 67.07 MPa, respectively. For treated fiber composites, water absorption increases with an increase in the duration of immersion in composites up to 144 h. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>(<b>a</b>) raw banyan (B) and banana (Ba) fibers. (<b>b</b>) The hardener (HY951) and epoxy resin (LY556).</p>
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<p>(<b>a</b>) Cutting of banyan and banana fibers. (<b>b</b>) The treated fibers of banyan and banana.</p>
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<p>(<b>a</b>) the fibers are stagnating. (<b>b</b>) Vacuum bag process.</p>
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<p>Schematic layout of the ply sequence for banyan (B) and banana (Ba) fiber epoxy hybrid composites. (<b>a</b>) 25B/25Ba, (<b>b</b>) 30B/20Ba and (<b>c</b>) 35B/15Ba.</p>
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<p>(<b>a</b>) Laminate composite, (<b>b</b>) Tensile test composite specimens 30 and (<b>c</b>) Bending test specimens.</p>
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<p>(<b>a</b>) A servo-hydraulic-type Nano Plug-n’-Play Series Universal testing machine. (<b>b</b>) Three-point bend fixture.</p>
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<p>Tensile strength variation of natural fiber reinforced without treatment composite for different volume fractions and different orientations.</p>
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<p>Tensile load carrying capacity of natural fiber reinforced with and without treatment composite for different volume fractions and different orientations.</p>
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<p>Flexural strength variation of natural fiber reinforced with treatment composite for different volume fractions and different orientations.</p>
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<p>Bending load carrying capacity of natural fiber reinforced with and without treatment composites for different volume fractions and different orientations.</p>
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<p>Water absorption curves (<b>a</b>) untreated banyan and banana fiber-reinforced composites and (<b>b</b>) treated banyan and banana fiber-reinforced composites.</p>
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<p>Simulated tensile and flexural stress distribution with different volume fractions and different orientations.</p>
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<p>Simulated tensile and flexural stress distribution with different volume fractions and different orientations.</p>
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<p>Simulated tensile and flexural stress distribution with different volume fractions and different orientations.</p>
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<p>Simulated tensile and flexural stress distribution with different volume fractions and different orientations.</p>
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<p>Simulated tensile and flexural stress distribution with different volume fractions and different orientations.</p>
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16 pages, 2795 KiB  
Article
Prediction of the Bond Strength of Externally Bonded FRP Sheets Applied to Concrete via Grooves Technique Using Artificial Neural Networks
by Abdelatif Salmi
J. Compos. Sci. 2024, 8(1), 30; https://doi.org/10.3390/jcs8010030 - 12 Jan 2024
Cited by 2 | Viewed by 2060
Abstract
The present study aims to fill a gap in the literature on the estimation of the bond strength of fiber reinforced polymer sheets bonded to concrete, via the externally bonded reinforcement on grooves (EBROG) technique, employing the curve-fitting on existing datasets in the [...] Read more.
The present study aims to fill a gap in the literature on the estimation of the bond strength of fiber reinforced polymer sheets bonded to concrete, via the externally bonded reinforcement on grooves (EBROG) technique, employing the curve-fitting on existing datasets in the literature and the methodology of Artificial Neural Networks (ANNs). Therefore, a dataset of 39 experimental results derived from EBROG technique is collected from the literature. A mathematical equation for the bond strength of FRP sheets applied on concrete via the EBROG technique was suggested using curve-fitting and general regression. The proposed mathematical equation is compared and validated with experimental results. The developed ANN model was constructed after testing diverse hidden layers and neurons to find the optimal predictions. The validation of the model is carried out using the experimental results and a statistical analysis is applied to assess the proposed mathematical equation and the proposed ANN model. Furthermore, a parametric study using the ANN model was also performed to investigate the influence of various factors on the bond strength of FRP sheets bonded to concrete. The parametric study proves that the bond strength increases with increasing the tensile stiffness per width, the FRP sheet width, and the concrete compressive strength; however, the effect of the Groove’s width and depth is found to be not monotonous. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Assessment of the mathematical equation.</p>
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<p>Histograms of experimental and predicted results.</p>
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<p>Estimates of various ANN models with one hidden layer.</p>
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<p>Assessment of the ANN model with four neurons in one hidden layer.</p>
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<p>Estimates of various ANN models with two hidden layers.</p>
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<p>Assessment of the ANN model with 4 neurons in 1st hidden layer and 5 in the 2nd layer.</p>
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<p>Structure of recommended ANN model.</p>
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<p>Variation of the mean square error as a function of the epochs.</p>
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<p>Parametric study outcomes for the FRP/Concrete bond strength.</p>
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13 pages, 10066 KiB  
Article
Development and Characterization of Flax–Gypsum Composites
by Vamsi Chakarala, Jens Schuster and Yousuf Pasha Shaik
J. Compos. Sci. 2024, 8(1), 27; https://doi.org/10.3390/jcs8010027 - 11 Jan 2024
Cited by 2 | Viewed by 2101
Abstract
Flax–gypsum composites are an emerging class of environmentally friendly materials that combine the mechanical properties of gypsum with the advantageous characteristics of flax fibers. The production of flax–gypsum composites involve the incorporation of flax fibers, derived from the flax plant, into gypsum matrix [...] Read more.
Flax–gypsum composites are an emerging class of environmentally friendly materials that combine the mechanical properties of gypsum with the advantageous characteristics of flax fibers. The production of flax–gypsum composites involve the incorporation of flax fibers, derived from the flax plant, into gypsum matrix systems. In order to create a uniform distribution of fibers within the gypsum matrix, the hand lay-up approach has been used to produce the specimens. The fiber content and orientation significantly influence the resulting mechanical and physical properties of the composites. Various tests were conducted on the samples, such as a flexural test, a compression test, a density test, a water absorption test, and a microscopy test. The addition of flax fibers imparts several desirable properties to the gypsum matrix. When combined with gypsum, these fibers enhanced the composite’s mechanical properties, such as flexural strength and compressive strength. The results indicated improved compression and flexural strengths due to effective load transfer within the matrix, for up to 10% of fiber loading. A decrease in composite density upon flax fiber addition results in a lighter material, enabling insights for various applications. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Types of molds (1), (2).</p>
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<p>Samples produced.</p>
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<p>Flexural modulus comparison with different samples.</p>
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<p>Flexural strength comparison of different samples.</p>
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<p>Flexural test curve of 85% gypsum and 15% flax fiber composite with 20 mm fiber length.</p>
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<p>Compression modulus comparison of different samples.</p>
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<p>Compression strength comparison of different samples.</p>
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<p>Compression test curve of 85% gypsum and 15% falx fiber composite with 20 mm fiber length.</p>
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<p>Density comparison of different samples.</p>
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<p>Water absorption comparison of different samples.</p>
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<p>Optical microscopy test image of 100% gypsum at 500 µm scale.</p>
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<p>(<b>a</b>) Optical microscopy test image of 95% gypsum and 5% flax (10 mm) at 500 µm. (<b>b</b>) Optical microscopy test image of 90% gypsum and 10% flax (10 mm) at 500 µm. (<b>c</b>) Optical microscopy test image of 85% gypsum and 15% flax (10 mm) at 500 µm. (<b>d</b>) Optical microscopy test image of 95% gypsum and 5% flax (20 mm) at 500 µm. (<b>e</b>) Optical microscopy test image of 90% gypsum and 10% flax (20 mm) at 500 µm. (<b>f</b>) Optical microscopy test image of 85% gypsum and 15% flax (20 mm) at 500 µm scale.</p>
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16 pages, 14588 KiB  
Article
Quasi-Static Fracture Toughness and Damage Monitoring in Liquid Metal Reinforced Hybrid Composites
by Zachary Safford, Mohammed Shonar and Vijaya Chalivendra
J. Compos. Sci. 2024, 8(1), 25; https://doi.org/10.3390/jcs8010025 - 11 Jan 2024
Cited by 1 | Viewed by 1800
Abstract
An experimental study is performed to investigate the quasi-static fracture toughness and damage monitoring capabilities of liquid metal (75.5% Gallium/24.5% Indium) reinforced intraply glass/carbon hybrid composites. Two different layups (G-0, where glass fibers are along the crack propagation direction; C-0, where carbon fibers [...] Read more.
An experimental study is performed to investigate the quasi-static fracture toughness and damage monitoring capabilities of liquid metal (75.5% Gallium/24.5% Indium) reinforced intraply glass/carbon hybrid composites. Two different layups (G-0, where glass fibers are along the crack propagation direction; C-0, where carbon fibers are along the crack propagation direction) and two different weight percentages of liquid metal (1% and 2%) are considered in the fabrication of the composites. A novel four-probe technique is employed to determine the piezo-resistive damage response under mode-I fracture loading conditions. The effect of layups and liquid metal concentrations on fracture toughness and changes in piezo-resistance response is discussed. The C-composite without liquid metal demonstrated higher fracture toughness compared to that of the G-composite due to carbon fiber breakage. The addition of liquid metal decreases the fracture initiation toughness of both G- and C-composites. Scanning electron microscopy images show that liquid metal takes the form of large liquid metal pockets and small spherical droplets on the fracture surfaces. In both C- and G-composites, the peak resistance change of composites with 2% liquid metal is substantially lower than that of both no-liquid metal and 1% liquid metal composites. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Fabrication process for liquid metal dispersion and the vacuum infusion process.</p>
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<p>Schematics of the two composite orientations are C (carbon fibers are in the crack propagation direction) and G (glass fibers are in the crack propagation direction).</p>
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<p>Diagram of DCB specimen configuration, with (<b>a</b>) showing the side view with voltage probes, (<b>b</b>) showing the top view with current probes, (<b>c</b>) showing a 3D view of the specimen where the voltage probes go around the crack faces, and (<b>d</b>) showing a side view of the actual test specimen.</p>
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<p>Schematic of the experimental setup used for fracture experimentation that includes the electrical measurement system.</p>
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<p>Delaminated sections of the actual test sample after failure for C-0%, C-1%, and C-2%.</p>
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<p>Delaminated sections of actual test samples after failure for G-0%, G-1%, and G-2%.</p>
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<p>Schematic of DCB specimen with dimensions associated with piano hinges used in Equations (2) and (3).</p>
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<p>Initial resistance for each composite configuration.</p>
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<p>Force-displacement and electrical resistance change plots of experiments for samples (<b>a</b>) C–0%, (<b>b</b>) C-1%, and (<b>c</b>) C-2%.</p>
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<p>Force-displacement and electrical resistance change plots of experiments for samples (<b>a</b>) G-0%, (<b>b</b>) G-1%, and (<b>c</b>) G-2%.</p>
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<p>Fracture toughness initiation values for each composite configuration.</p>
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<p>SEM images of the fracture surfaces of (<b>a</b>) C-0%, (<b>b</b>) C-1%, (<b>c</b>) C-2%, and (<b>d</b>) the magnified regions of C-2%.</p>
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<p>SEM images of the fracture surfaces of (<b>a</b>) G-0%, (<b>b</b>) G-2%, and (<b>c</b>,<b>d</b>) the magnified regions of G-2%.</p>
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<p>Characteristic plots of force vs. displacement plots, including zoomed regions for (<b>a</b>) C-0%, (<b>b</b>) C-1%, and (<b>c</b>) C-2%.</p>
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<p>Characteristic plots of force vs. displacement plots, including zoomed regions for (<b>a</b>) G-0%, (<b>b</b>) G-1%, and (<b>c</b>) G-2%.</p>
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14 pages, 3920 KiB  
Article
Finite Element Modelling of the Effect of Adhesive Z-Connections on the Swelling of a Laminated Wood Composite
by Mohammad Sadegh Mazloomi, Wenchang He and Philip David Evans
J. Compos. Sci. 2023, 7(10), 442; https://doi.org/10.3390/jcs7100442 - 18 Oct 2023
Cited by 2 | Viewed by 1825
Abstract
This study used finite element analysis (FEA) to model the effects of adhesive Z-connections on the thickness swelling of laminated wood composites exposed to water. We hypothesized that the area density, diameter, and spatial distribution of adhesive Z-connections will influence the ability of [...] Read more.
This study used finite element analysis (FEA) to model the effects of adhesive Z-connections on the thickness swelling of laminated wood composites exposed to water. We hypothesized that the area density, diameter, and spatial distribution of adhesive Z-connections will influence the ability of Z-connections to restrain thickness swelling of the composites. We tested this hypothesis by modelling a wood composite in ANSYS FEA software v. 17.0 to explore the effect of moisture on the thickness swelling of the wood composite. The results were compared with those obtained experimentally. We then examined the effect of the area density, size (diam.), and spatial distribution of the adhesive Z-connections on the thickness swelling of wood composites. Our results showed a positive correlation between the number of adhesive Z-connections in the composites and restriction of thickness swelling following 72 h of simulated moisture diffusion. Similarly, increasing the size of adhesive Z-connections also restricted thickness swelling. In contrast, different spatial distributions of Z-connections had little effect on restraining thickness swelling. Our modelling approach opens up opportunities for more complex designs of adhesive Z-connections, and also to examine the effect of wood properties, such as permeability, density, and hygroscopic swelling ratios on the thickness swelling of laminated wood composites. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Schematic illustration of veneer lay-up and hole pattern.</p>
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<p>Definition of X–Y–Z coordinate system and schematic illustration of the symmetry of the modelled material (arrowed blue) and water absorption planes (arrowed red) in the model.</p>
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<p>(<b>a</b>) Simulated-moisture-content change over time in the core of the model wood composite. (<b>b</b>) 3D moisture distribution in 1/8 of the model wood composite after 72 h (3 days) of simulated water soaking. W = 0 (completely dry), a red colour indicates W = 1 (completely saturated).</p>
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<p>Simulated thickness swelling after 24 h, and confocal profilometry scans of the surface after 24 h of immersion in water. Note that the FE model is 1/8 of the model wood composite.</p>
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<p>Z-direction deformation in 1/8 of the model wood composites containing 4, 16, 20, 36, and 48 adhesive Z-connections; (<b>a–e</b>) after 24 h simulated immersion in water; (<b>f</b>–<b>j</b>) after 72 h simulated immersion in water. Note that the maximum in the Figure is 1.09 as it is 1/8 of the model wood composite. This number should be doubled in order to reach the correct thickness swelling.</p>
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<p>Z-direction deformation in 1/8 of model wood composite containing simulated adhesive Z-connections with different diameters; (<b>a</b>–<b>c</b>) after 24 h simulated immersion in water; (<b>d</b>–<b>f</b>) after 72 h simulated immersion in water.</p>
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<p>Z-direction deformation in 1/8 of a model wood composite containing 16 and 20 simulated adhesive Z-connections with different spatial distributions; (<b>a</b>–<b>d</b>) after 24 h simulated immersion in water; (<b>e</b>–<b>h</b>) after 72 h simulated immersion in water.</p>
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21 pages, 18024 KiB  
Article
The Intra-Ply Shear Behaviour of Non-Isothermal Thermoplastic Composite Laminates
by George E. Street and Michael S. Johnson
J. Compos. Sci. 2023, 7(10), 432; https://doi.org/10.3390/jcs7100432 - 13 Oct 2023
Cited by 1 | Viewed by 1902
Abstract
During the thermoforming of fibre-reinforced thermoplastic (FRTP) organosheets, the desire to minimise tool temperatures leads to non-isothermal temperature profiles through the laminate thickness. The aim of this study was to understand the influence of these non-isothermal conditions on FRTP intra-ply shearing. Novel non-isothermal [...] Read more.
During the thermoforming of fibre-reinforced thermoplastic (FRTP) organosheets, the desire to minimise tool temperatures leads to non-isothermal temperature profiles through the laminate thickness. The aim of this study was to understand the influence of these non-isothermal conditions on FRTP intra-ply shearing. Novel non-isothermal bias extension tests were conducted, revealing that an average between the isothermal shear curves of both laminate faces approximately represented the respective non-isothermal condition. However, these findings were irrespective of FRTP thickness, and only applied to laminates that wholly remained above the crystallisation onset temperature. Upon the onset of crystallisation in a single ply, the non-isothermal shear resistance skewed heavily towards that (within 5%) of the crystallised ply and inhomogeneous shear angles were observed. Non-isothermal thermoforming validated these findings with the presence of wrinkles on non-isothermal hemispheres in which a single ply had reached crystallisation. This reaffirms the importance of accurate thermal monitoring during FRTP processing. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>CF-PA6 differential scanning calorimetry (DSC) results.</p>
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<p>Undeformed (<b>left</b>) and deformed (<b>right</b>) specimen for a woven or cross-ply laminate in the bias extension test.</p>
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<p>Non-isothermal bias extension testing experimental setup.</p>
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<p>Thermal history for 270 °C and 230 °C isothermal and non-isothermal laminates. Thick solid lines indicate the whole laminate, thin solid lines indicate the hot face temperature and thin dashed lines indicate the cold face temperature.</p>
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<p>Relationship between shear angle and axial displacement of 4-ply, 250 °C (isothermal), 100 mm/min bias extension specimens at 20 mm, 30 mm and 40 mm displacement, respectively.</p>
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<p>Through-section profiles taken from the centre of non-isothermal bias extension specimen samples (<b>a</b>) above crystallisation onset and (<b>b</b>) at crystallisation onset.</p>
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<p>Isothermal forces versus displacement results for 4-ply laminates at 100 mm/min displacement at (<b>a</b>) all tested temperatures and (<b>b</b>) temperatures greater than the crystallisation onset point.</p>
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<p>Normalised shear stress versus shear-angle experimental data for bias extension tests of 4- and 8-ply laminates at 100 mm/min and varying temperatures at temperatures above the crystallisation onset point.</p>
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<p>Isothermal and non-isothermal shear stress versus shear angle experimental data for (<b>a</b>) 4-ply laminates at crystallisation onset, (<b>b</b>) 4-ply laminates above crystallisation onset, (<b>c</b>) 8-ply laminates at crystallisation onset and (<b>d</b>) 8-ply laminates above crystallisation onset.</p>
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<p>Shear factor versus effective temperature for (<b>a</b>) temperatures at crystallisation onset and (<b>b</b>) temperatures above crystallisation onset. For non-isothermal results, line colour represents hot-side temperature, and line style represents cold-side temperature.</p>
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<p>Effective temperature ratio (effective temperature as a percentage between the respective hot and cold sides) for all non-isothermal bias extension tests.</p>
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<p>Assumed out-of-plane thermal distribution for a non-isothermal laminate that may be expected between bias extension experiments and real-world thermoforming conditions.</p>
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<p>Novel hemispherical punch apparatus mounted to the universal testing machine.</p>
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<p>Scanned hemispheres overlaid with MATLAB<sup>®</sup> shear angle output for non-isothermal thermoforming: hot face at 250 °C and cold face at (<b>a</b>) 230 °C, (<b>b</b>) 150 °C, (<b>c</b>), 130 °C and (<b>d</b>) 110 °C.</p>
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24 pages, 12336 KiB  
Article
A Comparison of Three Simulation Techniques for Modeling the Fan Blade–Composite Abradable Rub Strip Interaction in Turbofan Engines
by Aleksandr Cherniaev
J. Compos. Sci. 2023, 7(9), 389; https://doi.org/10.3390/jcs7090389 - 14 Sep 2023
Cited by 1 | Viewed by 2311
Abstract
Turbofan engine models for foreign object impact simulations must include a representation of fan blade interactions with surrounding components of the engine, including rubbing against the abradable lining. In this study, three numerical techniques, namely, the finite element method (FEM), smoothed particles hydrodynamics [...] Read more.
Turbofan engine models for foreign object impact simulations must include a representation of fan blade interactions with surrounding components of the engine, including rubbing against the abradable lining. In this study, three numerical techniques, namely, the finite element method (FEM), smoothed particles hydrodynamics (SPH), and the adaptive (hybrid) FEM/SPH approach (ADT), were evaluated for their applicability to modeling of the blade–abradable rub strip (ARS) interaction. Models developed using these methods in the commercial code LS-DYNA were compared in terms of their computational cost, robustness, sensitivity to mesh density, and certain physical and non-physical parameters. As a result, the applicability of the models to represent the blade-ARS interaction was ranked as follows (1—most applicable, 3—least applicable): 1—SPH, 2—FEM, and 3—ADT. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Layout of a fan section of a generic turbofan engine.</p>
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<p>An example of a representative rub morphology and the grid used in calculations of damaged area.</p>
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<p>Peak force, average force, and process duration of the first rub.</p>
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<p>The generic abradable material microstructure: hollow glass microspheres dispersed in a polymer matrix. (<b>a</b>) Optical microscopy (a hollow structure of particles is noted); (<b>b</b>) scanning electron microscopy (a high volume fraction of particles is noted).</p>
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<p>Experimentally observed behavior of abradable materials under tensile and confined compression loading. (<b>a</b>) Uniaxial tension; (<b>b</b>) confined compression.</p>
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<p>Pressure–volumetric strain relationship for the EOS of the abradable material.</p>
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<p>Virtual confined compression test: (<b>a</b>) setup (sectioned view); (<b>b</b>) force–displacement graph.</p>
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<p>A numerical model for simulating the blade–ARS interactions.</p>
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<p>Implementation of the forced blade excursion in the numerical model (relative coordinates define the fraction of the maximum excursion depth).</p>
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<p>Abradable representation using the FEM, ADT, and SPH methods (the horizontal line defines the position of the tray; a—the thickness of ARS).</p>
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<p>The influence of the SHLEDG parameter on the interaction of a shell element and a solid element modeled using a segment-based contact (option SOFT = 2).</p>
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<p>The effect of shell edge treatment on the results of blade rub simulations (SPH models: contour plot shows effective strain in the range from 0 [blue] to 0.1 [red]).</p>
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<p>Predicted rub zone morphology as a function of the element size.</p>
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<p>The effect of the element/particle size on the rub force prediction. (<b>a</b>) Finite element method (FEM); (<b>b</b>) adaptive FEM/SPH technique; (<b>c</b>) smoothed particles hydrodynamics (SPH) model.</p>
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<p>Model metrics as a function of the element size.</p>
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<p>Rub zone morphology for the equivalent element size, EES (<b>left</b>), and the equivalent computational time, ECT (<b>right</b>) finite element models. (<b>a</b>) EES FE model; (<b>b</b>) ECT FE model.</p>
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<p>Contact forces for the “equivalent element size” (2.54 mm elements) and the “equivalent computational time” (1.02 mm elements) finite element models.</p>
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<p>The influence of erosion strain on the prediction of contact force and morphology of the rub. (<b>a</b>) The EES finite element model (element size: 2.54 mm); (<b>b</b>) the ECT finite element model (element size: 1.02 mm); (<b>c</b>) the adaptive method.</p>
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<p>The influence of erosion strain on the prediction of contact force and morphology of the rub. (<b>a</b>) The EES finite element model (element size: 2.54 mm); (<b>b</b>) the ECT finite element model (element size: 1.02 mm); (<b>c</b>) the adaptive method.</p>
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<p>Variation in the process metrics as a function of erosion strain. (<b>a</b>) Average rub force; (<b>b</b>) process duration; (<b>c</b>) damaged area.</p>
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<p>Force–time response of the models as a function of the rub depth. (<b>a</b>) FEM, EES model (filtered); (<b>b</b>) FEM, ECT model (not filtered); (<b>c</b>) adaptive method (filtered); (<b>d</b>) SPH technique (not filtered).</p>
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<p>Process metrics as a function of the rub depth. (<b>a</b>) Average rub force; (<b>b</b>) process duration; (<b>c</b>) damaged area (first rub); (<b>d</b>) total damaged area.</p>
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<p>Force–time response of the models as a function of the friction coefficient. (<b>a</b>) FEM, EES model (filtered); (<b>b</b>) FEM, ECT model (not filtered); (<b>c</b>) adaptive method (filtered); (<b>d</b>) SPH technique (not filtered).</p>
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<p>Force–time response of the models as a function of the friction coefficient. (<b>a</b>) FEM, EES model (filtered); (<b>b</b>) FEM, ECT model (not filtered); (<b>c</b>) adaptive method (filtered); (<b>d</b>) SPH technique (not filtered).</p>
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<p>Contact between the blade and the ARS.</p>
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<p>Acceleration of node #85 on the tip of the blade. (<b>a</b>) Tip node acceleration as a function of the modeling method; (<b>b</b>) tip node acceleration as a function of the contact viscous damping coefficient (VDC); (<b>c</b>) tip node acceleration as a function of the element size.</p>
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<p>Acceleration of node #85 on the tip of the blade. (<b>a</b>) Tip node acceleration as a function of the modeling method; (<b>b</b>) tip node acceleration as a function of the contact viscous damping coefficient (VDC); (<b>c</b>) tip node acceleration as a function of the element size.</p>
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16 pages, 5431 KiB  
Article
Mechanical Properties of Uncured Thermoset Tow Prepreg: Experiment and Finite Element Analysis
by Mina Derakhshani Dastjerdi, Massimo Carboni and Mehdi Hojjati
J. Compos. Sci. 2023, 7(8), 312; https://doi.org/10.3390/jcs7080312 - 29 Jul 2023
Cited by 1 | Viewed by 2012
Abstract
This paper presents an experimental analysis of the tensile behavior of unidirectional carbon/epoxy prepreg, focusing on the nonlinearity observed at the beginning of the stress–strain curve. Due to the material’s high viscosity, securely holding specimens during testing was challenging, prompting modifications in the [...] Read more.
This paper presents an experimental analysis of the tensile behavior of unidirectional carbon/epoxy prepreg, focusing on the nonlinearity observed at the beginning of the stress–strain curve. Due to the material’s high viscosity, securely holding specimens during testing was challenging, prompting modifications in the gripping method to ensure reliable data. By using a longer gauge length, the slippage impact on elastic modulus measurement was minimized, resulting in good repeatability among the test samples. Experimental findings highlighted the significant interaction between fiber waviness and the viscous matrix, leading to stiffness reduction. The linear stiffness of the samples closely matched that of the fibers and remained unaffected by temperature variations. However, at higher temperatures, the epoxy matrix’s decreased viscosity caused an upward shift in the stiffness plot within the non-linear region. To support the experimental findings, a micromechanical model of prepreg tow with fiber waviness was proposed. An RVE model of periodically distributed unidirectional waved cylindrical fibers embedded within the matrix was developed to predict effective material stiffness parameters. The simulation outcomes aligned well with the uniaxial tensile test of the prepreg tow, demonstrating the proposed RVE model’s capability to accurately predict elastic properties, considering factors like fiber arrangement, waviness, and temperature. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Tensile test setup.</p>
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<p>Width reduction of the sample.</p>
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<p>Tensile behavior of various gauge lengths tested under ambient conditions.</p>
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<p>(<b>a</b>) Geometry of the wavy fiber. (<b>b</b>) RVE model with square arrangement.</p>
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<p>Finite element model of the RVE.</p>
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<p>Average experimental results of the tensile behavior of uncured prepreg.</p>
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<p>Trendline fit to the non-linear region.</p>
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<p>Linear trendline fit to non-linear region.</p>
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<p>Engineering stress–strain curves from the tensile test at various temperatures.</p>
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<p>Effective elastic material properties according to the fiber waviness for hexagonal, diamond, and square arrays. (<b>a</b>) Longitudinal Young’s modulus E<sub>1</sub>, (<b>b</b>) transverse Young’s modulus E<sub>2</sub>, (<b>c</b>) shear modulus G<sub>12</sub>, (<b>d</b>) shear modulus G<sub>23</sub>, (<b>e</b>) Poisson’s ratio <span class="html-italic">ν</span><sub>12</sub>, and (<b>f</b>) Poisson’s ratio <span class="html-italic">ν</span><sub>23</sub>.</p>
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<p>Effective longitudinal Young’s modulus (E<sub>1</sub>) according to fiber waviness at different values of matrix stiffness.</p>
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15 pages, 4638 KiB  
Article
An Efficient Method for Simulating the Temperature Distribution in Regions Containing YAG:Ce3+ Luminescence Composites of White LED
by Quang-Khoi Nguyen and Thi-Hanh-Thu Vu
J. Compos. Sci. 2023, 7(7), 301; https://doi.org/10.3390/jcs7070301 - 22 Jul 2023
Cited by 3 | Viewed by 1597
Abstract
A thermal model was built to estimate the temperature distribution in the hemispherical packaging volume of a white LED at a steady state. Inherent heat sources appeared in the white LED when its power was measured. A simplified 3D to 2D space process [...] Read more.
A thermal model was built to estimate the temperature distribution in the hemispherical packaging volume of a white LED at a steady state. Inherent heat sources appeared in the white LED when its power was measured. A simplified 3D to 2D space process that improves the model and solves the heat diffusion equation in a simpler and faster manner is presented. The finite element method was employed using MATLAB software (version R2017b) to identify the temperature distribution. The model was applied for different values of injection current, including 50 mA, 200 mA, 350 mA, and 500 mA. The influence of the injection current and thermal conductivity difference on the temperature distribution of the encapsulant, blue LED die, and substrate region was clearly observed. The results indicate that white light packaging technology should locate phosphor far from the LED die, that the thermal conductivity of the silicone–phosphor region should be improved, that heat should be dissipated for pc-WLEDs when using a high operating power, and that the injection current should be kept as moderate as possible. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Geometry of white light pc-LED using a hemispherical structure.</p>
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<p>Difference in excitation and converted wavelengths.</p>
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<p>Mechanism of heat generation inside the blue LED die.</p>
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<p>Graphical illustration of the simplified process (3D to 2D) of building the thermal modeling process: (<b>a</b>) 3D view of pcW-LED phosphor dome packaged structure; (<b>b</b>) cross section at plane (x–z) and (y–z); (<b>c</b>,<b>d</b>) indicate the similarity between the cross sections at plane (x–z) and (y–z).</p>
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<p>The process of boundary condition determination.</p>
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<p>The main steps of the simulation.</p>
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<p>The 2D structure of the pc-WLED.</p>
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<p>Finite element method meshed for 2D geometry of the pc-WLED.</p>
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<p>Temperature distributions at steady state corresponding to different injection electrical currents: (<b>a</b>) 50 mA, (<b>b</b>) 200 mA, (<b>c</b>) 350 mA, and (<b>d</b>) 500 mA.</p>
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<p>Temperature distributions at steady state corresponding to different injection electrical currents: (<b>a</b>) 50 mA, (<b>b</b>) 200 mA, (<b>c</b>) 350 mA, and (<b>d</b>) 500 mA.</p>
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<p>(<b>a</b>) Sample of phosphor dome packaged structure, and (<b>b</b>) sample of phosphor dome packaged structure cut in half.</p>
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<p>Experimental setup for determination of the temperature distribution of a sample of phosphor dome packaged structure cut in half (<b>left</b>), and enlarged area (<b>right</b>).</p>
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<p>Temperature distribution at steady state corresponding to different injection electrical currents: (<b>a</b>) 50 mA and (<b>b</b>) 200 mA.</p>
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13 pages, 3999 KiB  
Article
Statistical Analysis and Optimization of the Experimental Results on Performance of Green Aluminum-7075 Hybrid Composites
by Olanrewaju Seun Adesina, Abayomi Adewale Akinwande, Oluwatosin Abiodun Balogun, Adeolu Adesoji Adediran, Olufemi Oluseun Sanyaolu and Valentin Romanovski
J. Compos. Sci. 2023, 7(3), 115; https://doi.org/10.3390/jcs7030115 - 13 Mar 2023
Cited by 12 | Viewed by 2063
Abstract
The present study assessed the potential of engaging response surface analysis in the experimental design, modeling, and optimization of the strength performance of aluminum-7075 green composite. The design of the experiment was carried out via the Box–Behnken method and the independent variables are [...] Read more.
The present study assessed the potential of engaging response surface analysis in the experimental design, modeling, and optimization of the strength performance of aluminum-7075 green composite. The design of the experiment was carried out via the Box–Behnken method and the independent variables are rice husk ash (RHA) at 3–12 wt.%, glass powder (GP) at 2–10 wt.%, and stirring temperature (ST) at 600–800 °C. Responses examined are yield, ultimate tensile, flexural, and impact strengths, as well as microhardness and compressive strength. ANOVA analysis revealed that the input factors had consequential contributions to each response, eventually presenting regression models statistically fit to represent the experimental data, further affirmed by the diagnostic plots. The result of the optimization envisaged an optimal combination at 7.2% RHA, 6.2 GP, and 695 °C with a desirability of 0.910. A comparison between the predicted values for the responses and the values of the validation experiment revealed an error of <5% for each response. Consequently, the models are certified adequate for response predictions at 95% confidence, and the optimum combination is adequate for the design of the composite. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Response surface revealing effects of interaction of rice husk ash vs. glass powder at 700 °C constant temperature on (<b>a</b>) yield strength, (<b>b</b>) ultimate tensile strength, (<b>c</b>) flexural strength, (<b>d</b>) microhardness, (<b>e</b>) impact strength, (<b>f</b>) compressive strength.</p>
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<p>Response surface revealing effects of interaction of rice husk ash vs. stirring temperature at 6% constant GP dosage on (<b>a</b>) yield strength, (<b>b</b>) ultimate tensile strength, (<b>c</b>) flexural strength, (<b>d</b>) microhardness, (<b>e</b>) impact strength, (<b>f</b>) compressive strength.</p>
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<p>Response surface revealing effects of interaction of glass powder vs. stirring temperature at 7.5% RHA constant loading on (<b>a</b>) yield strength, (<b>b</b>) ultimate tensile strength, (<b>c</b>) flexural strength, (<b>d</b>) microhardness, (<b>e</b>) impact strength, (<b>f</b>) compressive strength.</p>
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<p>Optimization ramp indicating optimum combination and predicted responses at desirability of 0.910.</p>
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12 pages, 2505 KiB  
Article
A Mathematical Approach for Sound Insulation Characteristics and Cost Optimization of Double-Layer Composite Structures
by Liang Zhang, Huawei Zhang, Qiyu Chen and Danfeng Long
J. Compos. Sci. 2023, 7(3), 110; https://doi.org/10.3390/jcs7030110 - 9 Mar 2023
Cited by 3 | Viewed by 2760
Abstract
The compressor is the primary source of noise in a refrigeration system. Most compressors are wrapped with multi-layer sound insulation cotton for noise reduction and sound insulation. We explore the sound insulation law of different polyvinyl chloride thicknesses and non-woven fibers. Polyvinyl chloride [...] Read more.
The compressor is the primary source of noise in a refrigeration system. Most compressors are wrapped with multi-layer sound insulation cotton for noise reduction and sound insulation. We explore the sound insulation law of different polyvinyl chloride thicknesses and non-woven fibers. Polyvinyl chloride with varying thicknesses and non-woven fibers are then combined by bonding to study the sound insulation characteristics of a two-layer composite structure. A sound insulation prediction model is established using the multi-parameter nonlinear regression method. An optimal cost mathematical model is established based on experimental and mathematical methods that can quickly determine the optimal cost scheme for different designs with the same effect. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Schematic diagram of double-layer sound insulation structures.</p>
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<p>Schematic diagram of the sound insulation test for the sound insulation structure.</p>
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<p>Schematic diagram of noise and vibration acquisition.</p>
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<p>Comparison between the predicted and experimental values of the mathematical model for the rapid calculation of sound insulation.</p>
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<p>Optimal cost calculation model diagram.</p>
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<p>Parameter combinations meeting the sound insulation conditions (3D plot).</p>
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<p>Parameter combinations meeting the sound insulation conditions (2D plot).</p>
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<p>Cost corresponding to the parameter combination scheme.</p>
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<p>Cost diagram meeting the parameters of 22 dB (A) sound insulation.</p>
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23 pages, 4426 KiB  
Article
Characterization of UV Light Curable Piezoelectric 0-0-3 Composites Filled with Lead-Free Ceramics and Conductive Nanoparticles
by Rytis Mitkus, Lena Piechowiak and Michael Sinapius
J. Compos. Sci. 2023, 7(2), 89; https://doi.org/10.3390/jcs7020089 - 20 Feb 2023
Cited by 5 | Viewed by 2681
Abstract
Lead-free piezoelectric materials are essential for our healthy future but offer lower performance than lead-based materials. Different material combinations are explored to improve the performance of lead-free materials. By filling the UV light curable photopolymer resin with 30 vol.% lead-free piezoelectric ceramics and [...] Read more.
Lead-free piezoelectric materials are essential for our healthy future but offer lower performance than lead-based materials. Different material combinations are explored to improve the performance of lead-free materials. By filling the UV light curable photopolymer resin with 30 vol.% lead-free piezoelectric ceramics and with up to 0.4 wt.% conductive nanofillers, thin and flexible piezoelectric 0-0-3 composites are formed. Two particle sizes of Potassium Sodium Niobate (KNN) and Barium Titanate (BTO) ceramics were used with four conductive nanofillers: Graphene Nanoplatelets (GNPs), Multi-Walled Carbon Nanotubes (MWCNTs), and two types of Graphene Oxide (GO). Resulting high viscosity suspensions are tape-cast in a mold as thin layers and subsequently exposing them to UV light, piezoelectric composite sensors are formed in 80 s. Even low nanofiller concentrations increase relative permittivities, however, they strongly reduce curing depth and increase undesirable dielectric losses. Non-homogeneous dispersion of nanofillers is observed. In total, 36 different compositions were mixed and characterized. Only six selected material compositions were investigated further by measuring mechanical, dielectric, and piezoelectric properties. Results show KNN composite performance as piezoelectric sensors is almost six times higher than BTO composite performance. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Curing depth over curing time of all composites manufactured in the study at room temperature.</p>
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<p>Microstructure of: (<b>A</b>) 30KNN6 (<math display="inline"><semantics> <mrow> <mo>×</mo> <mn>20</mn> <mo>,</mo> <mn>000</mn> </mrow> </semantics></math>), (<b>B</b>) 30BTO13 (<math display="inline"><semantics> <mrow> <mo>×</mo> <mn>10</mn> <mo>,</mo> <mn>000</mn> </mrow> </semantics></math>). Yellow circles show clearly visible missing particles.</p>
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<p>Room temperature relative permittivities <math display="inline"><semantics> <msub> <mi>ε</mi> <mi>r</mi> </msub> </semantics></math> and dielectric losses (dissipation factors <math display="inline"><semantics> <mrow> <mi>t</mi> <mi>a</mi> <mi>n</mi> <mi>δ</mi> <mo>)</mo> </mrow> </semantics></math> of all piezoelectric composites made in this study at 1 kHz. The data are not comparable with the literature since no electrodes were applied to the composites. Measurement points are joined with linear lines for visual purposes only and do not present a linear trend.</p>
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<p>Room temperature dielectric properties of piezoelectric composites, with applied silver ink electrodes, before poling at 1 kHz: (<b>A</b>) relative permittivities; (<b>B</b>) dielectric losses.</p>
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<p>Young’s modulus of solidified piezoelectric composites filled with: (<b>A</b>) KNN6 ceramic; (<b>B</b>) BTO13 ceramic.</p>
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<p>Performance of solidified piezoelectric composite materials: (<b>A</b>) piezoelectric charge coefficient <math display="inline"><semantics> <msub> <mi>d</mi> <mn>31</mn> </msub> </semantics></math> (reversed from negative for visualization); (<b>B</b>) piezoelectric voltage coefficient <math display="inline"><semantics> <msub> <mi>g</mi> <mn>31</mn> </msub> </semantics></math> (reversed from negative for visualization); (<b>C</b>) sensitivity.</p>
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13 pages, 19409 KiB  
Article
Micro-Scale Model of rCF/PA6 Spun Yarn Composite
by Tobias Georg Lang, Mir Mohammad Badrul Hasan, Anwar Abdkader, Chokri Cherif and Thomas Gereke
J. Compos. Sci. 2023, 7(2), 66; https://doi.org/10.3390/jcs7020066 - 6 Feb 2023
Cited by 2 | Viewed by 1920
Abstract
Recycling carbon fibers (rCF) for reuse is one approach to improve the sustainability of CFRP. However, until now, recycled carbon fiber plastics (rCFRP) had limited composite properties due to the microgeometry of the fibers, which made it difficult to use in load-bearing components. [...] Read more.
Recycling carbon fibers (rCF) for reuse is one approach to improve the sustainability of CFRP. However, until now, recycled carbon fiber plastics (rCFRP) had limited composite properties due to the microgeometry of the fibers, which made it difficult to use in load-bearing components. The production of hybrid yarns from rCF and PA6 fibers allows the fibers to be aligned. The geometric properties of the yarn and the individual fibers influence the mechanical properties of the composite. An approach for the modeling and simulation of hybrid yarns consisting of recycled carbon fibers and thermoplastic fibers is presented. The yarn unit cell geometry is modeled in the form of a stochastic fiber network. The fiber trajectory is modeled in form of helical curves using the idealized yarn model of Hearle et al. The variability in the fiber geometry (e.g., length) is included in form of statistical distributions. An additional compaction step ensures a realistic composite geometry. The created model is validated geometrically and by comparison with tensile tests of manufactured composites. With the validated model, multiple parameter studies investigating the influence of fiber and yarn geometry are carried out. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Micrograph of yarn with 30 t/m (<b>left</b>), identified fibers (<b>right</b>; yellow-PA6; blue-rCF).</p>
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<p>Idealized helical trajectory (based on [<a href="#B49-jcs-07-00066" class="html-bibr">49</a>]).</p>
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<p>RVE model generation steps: (<b>a</b>) Modeling overview, (<b>b</b>) Process diagram.</p>
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<p>Enforcing periodicity of cylinder element by splitting and translation.</p>
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<p>Test of intersection between new (blue) and existing (red) fibers.</p>
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<p>Modeled geometries with varying parameters: (<b>a</b>) orientation (<b>b</b>) waviness (<b>c</b>) twist (<b>d</b>) length.</p>
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<p>Tensile curve of Polyamide 6 fibers.</p>
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<p>Applied approach for Fiber-Matrix-Coupling (<b>a</b>) Domain Superposition Technique [<a href="#B42-jcs-07-00066" class="html-bibr">42</a>] (<b>b</b>) Coupled composite model.</p>
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<p>Geometrical validation of yarn geometry (<b>left</b>: micrograph of hybrid yarn with 30 t/m, <b>right</b>: modeled geometry with 30 t/m).</p>
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<p>Compaction simulation.</p>
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<p>Geometric validation of virtually compressed geometry (<b>left</b>) with micrograph of UD-composite (<b>right</b>) (both images yarn with 30 t/m).</p>
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<p>Tensile stress-strain-curve (grey-experiments; red-simulation).</p>
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<p>Axial fiber stresses during composite simulation of a yarn with 30 T/m (matrix elements hidden for clearity).</p>
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<p>Parameter study of yarn twist influence on composite properties.</p>
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<p>Parameter study of yarn packing fraction influence on composite properties.</p>
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<p>Parameter study of fiber length influence on composite properties (<b>left</b>—probability density functions of Weibull distribution, <b>right</b>—influence of Weibull shape parameter on composite properties).</p>
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<p>Parameter study of short fiber content influence on composite properties.</p>
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20 pages, 3351 KiB  
Article
Comparative Analysis of ANN-MLP, ANFIS-ACOR and MLR Modeling Approaches for Estimation of Bending Strength of Glulam
by Morteza Nazerian, Masood Akbarzadeh and Antonios N. Papadopoulos
J. Compos. Sci. 2023, 7(2), 57; https://doi.org/10.3390/jcs7020057 - 4 Feb 2023
Cited by 5 | Viewed by 1783
Abstract
Multiple linear regression (MLR), adaptive network-based fuzzy inference system–ant colony optimization algorithm hybrid (ANFIS-ACOR) and artificial neural network–multilayer perceptron (ANN-MLP) were tested to model the bending strength of Glulam (glue-laminated timber) manufactured with a plane tree (Platanus orientalis L.) wood [...] Read more.
Multiple linear regression (MLR), adaptive network-based fuzzy inference system–ant colony optimization algorithm hybrid (ANFIS-ACOR) and artificial neural network–multilayer perceptron (ANN-MLP) were tested to model the bending strength of Glulam (glue-laminated timber) manufactured with a plane tree (Platanus orientalis L.) wood layer adhered with different weight ratios (WR) of modified starch/urea formaldehyde (UF) adhesive containing different levels of nano-ZnO (NC) used at different levels of the press temperature (Tem) and time (Tim). According to X-ray diffraction (XRD) and stress–strain curves, some changes in the behavior of the product were seen. After selecting the best model through determining statistics such as the determination coefficient (R2) and root mean square error (RMSE), mean absolute error (MAE) and sum of squares error (SSE), the production process was optimized to obtain the highest modulus of rupture (MOR) using the Genetic Algorithm (GA) combined with MLP. It was determined that the MLP had the best accuracy in estimating the response. According to the MLP-GA hybrid, the optimum input values for obtaining the best response include: WR—49.1%, NC—3.385%, Tem—199.4 °C and Tim—19.974 min. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>The schematic structure of the ANN-MLP algorithm used.</p>
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<p>Comparison of the measured and predicted MOR (MPa) for the testing and all data sets using (<b>A</b>) MLR, (<b>B</b>) ACO<sub>R</sub> and (<b>C</b>) MLP.</p>
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<p>Comparison of the measured and predicted MOR (MPa) for the testing and all data sets using (<b>A</b>) MLR, (<b>B</b>) ACO<sub>R</sub> and (<b>C</b>) MLP.</p>
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<p>The comparison of the error values estimated by the MLR, ACO<sub>R</sub> and MLP.</p>
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<p>Direct effects of the independent variables on the MOR. <span class="html-italic">x</span><sub>1</sub>: WR; <span class="html-italic">x</span><sub>2</sub>: NC; <span class="html-italic">x</span><sub>3</sub>: Tem; <span class="html-italic">x</span><sub>4</sub>: Tim.</p>
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<p>The interactive effects of WR × NC (<b>a</b>), WR × Tem (<b>b</b>), WR × Tim (<b>c</b>), NC × Tem (<b>d</b>), NC × Tim (<b>e</b>) and Tem × Tim (<b>f</b>) on the MOR.</p>
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<p>Load versus deflection curves for the selected samples.</p>
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<p>The XRD pattern for the index adhesives.</p>
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12 pages, 2923 KiB  
Article
On the Influence of Fatigue Damage in Short-Fibre Reinforced Thermoplastic PBT GF30 on Its Residual Strength under High Strain Rates: An Approach towards Simulative Prediction
by Christian Witzgall, Patrick Steck and Sandro Wartzack
J. Compos. Sci. 2023, 7(1), 23; https://doi.org/10.3390/jcs7010023 - 10 Jan 2023
Cited by 3 | Viewed by 3155
Abstract
Only by using accurate material data can precise simulation results be achieved. This principle also and especially applies in the field of crash simulation. However, in the simulation of short-fibre reinforced thermoplastics, material parameters are usually used that originate from the material testing [...] Read more.
Only by using accurate material data can precise simulation results be achieved. This principle also and especially applies in the field of crash simulation. However, in the simulation of short-fibre reinforced thermoplastics, material parameters are usually used that originate from the material testing of as-new samples. In order to get closer to the condition on the roads, where not only new vehicles are driving, the influence of service loads on the crashworthiness has to be investigated. This paper reports on studies of PBT GF30, a polybutylene terephthalate reinforced with 30% glass fibres, in which fatigue damage was induced in the material by cyclic loading. The residual strength was then determined in a high-speed experiment and compared with the strength of virgin samples. In order to enable the usability of the findings in the simulation, a modified failure criterion was implemented that takes the previous fatigue damage into account. The prediction quality of the simulation model was compared with the experimental findings and it can be concluded that there is good agreement. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>A schematic illustration of the component design process chain for SFRT.</p>
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<p>Main steps of the modelling approach.</p>
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<p>Schematic experiment workflow for material characterization.</p>
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<p>Becker tension rod as used in experiments.</p>
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<p>Testing equipment: (<b>a</b>) High-speed tensile testing with a Zwick HTM 5020; (<b>b</b>) Cyclic testing with a servo-hydraulic pulser Zwick HCT 25.</p>
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<p>Camera setup with the GOM ARAMIS 3D HHS in the background, during the tensile test.</p>
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<p>Schematic illustration of the cyclic measuring procedure.</p>
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<p>Comparison of the stress–strain curve with various damaged specimens in 0° orientation.</p>
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<p>Comparison between the analytical model and the simulation implementation of the weakened material data.</p>
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<p>Recorded stress–strain curves of specimens with varying degrees of damage.</p>
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13 pages, 1664 KiB  
Article
Development of Prediction Models for the Torsion Capacity of Reinforced Concrete Beams Using M5P and Nonlinear Regression Models
by Sadiq N. Henedy, Ali H. Naser, Hamza Imran, Luís F. A. Bernardo, Mafalda M. Teixeira and Zainab Al-Khafaji
J. Compos. Sci. 2022, 6(12), 366; https://doi.org/10.3390/jcs6120366 - 2 Dec 2022
Cited by 8 | Viewed by 1930
Abstract
Torsional strength is related with one of the most critical failure types for the design and assessment of reinforced concrete (RC) members due to the complexity of the associated stress state and low ductility. Previous studies have shown that reliable methods to predict [...] Read more.
Torsional strength is related with one of the most critical failure types for the design and assessment of reinforced concrete (RC) members due to the complexity of the associated stress state and low ductility. Previous studies have shown that reliable methods to predict the torsional strength of RC beams are still needed, namely for over-reinforced and high-strength RC beams. This research aims to offer a novel set of models to predict the torsional strength of RC beams with a wide range of design attributes and geometries by using advanced M5P tree and nonlinear regression models. For this, a broad database with 202 experimental tests is used to generate highly reliable and resilient models. To build the models, three independent variables related with the properties of the RC beams are considered: concrete cross-section area (area enclosed within the outer perimeter of the cross-section), concrete compressive strength, and torsional reinforcement factor (which accounts for the type—longitudinal or transverse—amount, and yielding strength of the torsional reinforcement). In contrast to multiple nonlinear regression approaches, the findings show that the M5P tree approach has the best estimation in terms of both accuracy and safety. Furthermore, M5P model predictions are far more accurate and safer than the most prevalent design equations. Finally, sensitivity and parametric studies are used to confirm the robustness of the presented models. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>The M5 model tree (adapted from [<a href="#B42-jcs-06-00366" class="html-bibr">42</a>]).</p>
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<p>M5 tree flowchart.</p>
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<p>M5P algorithm-based tree developed to estimate the torsional resistance of RC beams.</p>
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<p>Comparison of the performance of (<b>a</b>) M5P and (<b>b</b>) MLNR models for the training and testing datasets.</p>
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<p>Relationship between the variables and the ratio of experimental to predicted torsional strength.</p>
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16 pages, 6994 KiB  
Article
Micromechanical Approach to Predict Mechanical Properties of Particulate-Dispersed Composites with Dissimilar Interfacial Phases
by Tomoyuki Fujii, Keiichiro Tohgo, Takahiro Omi and Yoshinobu Shimamura
J. Compos. Sci. 2022, 6(12), 356; https://doi.org/10.3390/jcs6120356 - 22 Nov 2022
Cited by 2 | Viewed by 1582
Abstract
The mechanical properties of composites are affected by their constituents. For the development of high-performance composites, it is expected that a technique will be developed which can predict the mechanical properties of composites based on the mechanical properties of their constituents. This study [...] Read more.
The mechanical properties of composites are affected by their constituents. For the development of high-performance composites, it is expected that a technique will be developed which can predict the mechanical properties of composites based on the mechanical properties of their constituents. This study developed a technique based on a micromechanical approach to predict the mechanical properties of composites with interfacial phases between reinforcements and matrix. A double-inclusion model (Hori and Nemat-Nasser, 1993) is effective for the solution of such problems, of which the validity remains unclear. Problems with a particle surrounded by an interfacial phase embedded in an infinite body were calculated via the model and finite element analysis to verify the model. It was found that the macroscopic average stress of the double inclusion could be accurately solved by the model, although the microscopic stress of each phase could not be calculated with high accuracy. Therefore, a micromechanical approach based on the model was formulated and applied to particulate-dispersed composites consisting of zirconia and titanium, and fabricated by spark plasma sintering, in which Ti oxides were created along the interface between zirconia and titanium. As a result, the elastic-plastic stress–strain curves of the composites could be predicted. The approach can investigate the mechanical properties of composites with various shapes of reinforcement surrounded by dissimilar materials in a matrix. It can be concluded that the approach is promising for the development of composites with an excellent mechanical performance. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Element distributions of Zr, Ti, and O in PSZ-Ti composite fabricated via SPS.</p>
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<p>Mechanical properties of PSZ-Ti composites fabricated via powder metallurgy technique [<a href="#B15-jcs-06-00356" class="html-bibr">15</a>]. (<b>a</b>) Bending stress–strain curves of composites with various volume fractions of Ti fabricated via SPS; (<b>b</b>) Young’s modulus as a function of volume fraction of Ti for composites obtained via HP and SPS.</p>
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<p>Schematic of PSZ-Ti composite fabricated via powder metallurgy technique [<a href="#B14-jcs-06-00356" class="html-bibr">14</a>,<a href="#B15-jcs-06-00356" class="html-bibr">15</a>].</p>
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<p>Modeling of PSZ and Ti oxide in an infinite medium of Ti matrix for DIM. (<b>a</b>) A double inclusion in an infinite medium; (<b>b</b>) problem equivalent to (<b>a</b>).</p>
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<p>Finite element meshes and boundary conditions of the model for evaluating the accuracy of DIM.</p>
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<p>Normal stress distribution in the vicinity of a double inclusion.</p>
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<p>Microscopic average stresses of Ω and Γ phases as functions of thicknesses of Γ phase.</p>
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<p>Macroscopic average normal stress of R phase with various thicknesses of the Γ phase. The stress <math display="inline"><semantics> <mrow> <msup> <mrow> <mo>⟨</mo> <mi>σ</mi> </mrow> <mi>y</mi> </msup> <mo>⟩</mo> <msub> <mrow/> <mi mathvariant="normal">R</mi> </msub> </mrow> </semantics></math> is normalized by the remote stress <math display="inline"><semantics> <mrow> <msup> <mi>σ</mi> <mo>∞</mo> </msup> </mrow> </semantics></math>.</p>
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<p>Modeling of a particulate-dispersed composite with double inclusions. (<b>a</b>) Original problem of a composite with double inclusions dispersed in infinite matrix; (<b>b</b>) a problem equivalent to (<b>a</b>); (<b>c</b>) a problem equivalent to (<b>b</b>).</p>
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<p>Young’s modulus as a function of volume fraction of Ti and Ti oxide (Ti<sub>2</sub>O). The cross marks denote the experimental results for the PSZ-Ti composites fabricated via SPS.</p>
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<p>Estimation of volume fractions of phases in PSZ-Ti composites fabricated via SPS.</p>
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<p>Comparison of estimated stress–strain curves of the PSZ-Ti composites with the experimental results. (<b>a</b>) Volume fraction of Ti and Ti<sub>2</sub>O of 25%; (<b>b</b>) volume fraction of Ti and Ti<sub>2</sub>O of 90%. The experimental data are the same data shown in <a href="#jcs-06-00356-f001" class="html-fig">Figure 1</a>a.</p>
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<p>Finite element analysis of double inclusion subjected to shear loading.</p>
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<p>Distribution of shear stress <span class="html-italic">τ <sup>xy</sup></span> in the vicinity of a double inclusion.</p>
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<p>Microscopic shear stresses of Ω and Γ phases with various thicknesses of the Γ phase. The microscopic average stress <math display="inline"><semantics> <mrow> <mo>⟨</mo> <msup> <mi>τ</mi> <mrow> <mi>x</mi> <mi>y</mi> </mrow> </msup> <mo>⟩</mo> </mrow> </semantics></math> of each phase is normalized by the remote stress <math display="inline"><semantics> <mrow> <msup> <mi>τ</mi> <mo>∞</mo> </msup> </mrow> </semantics></math>.</p>
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<p>Average shear stress of R phase (=Ω + Γ) with various thicknesses of the Γ phase. The microscopic average stress <math display="inline"><semantics> <mrow> <msub> <mrow> <mo>⟨</mo> <msup> <mi>τ</mi> <mrow> <mi>x</mi> <mi>y</mi> </mrow> </msup> <mo>⟩</mo> </mrow> <mi mathvariant="normal">R</mi> </msub> </mrow> </semantics></math> is normalized by the remote stress <math display="inline"><semantics> <mrow> <msup> <mi>τ</mi> <mo>∞</mo> </msup> </mrow> </semantics></math>.</p>
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13 pages, 3352 KiB  
Article
Investigation of Mechanical Properties of Coffee Husk-HDPE-ABS Polymer Composite Using Injection-Molding Method
by Berhanu Tolessa Amena, Holm Altenbach, Getechew Shunki Tibba and Nazia Hossain
J. Compos. Sci. 2022, 6(12), 354; https://doi.org/10.3390/jcs6120354 - 22 Nov 2022
Cited by 11 | Viewed by 3034
Abstract
Waste biomass-based natural fibers are being extensively researched nowadays as a composite material with various waste-based high-density polyethylene (HDPE) to utilize the waste biomass and recycle the plastic waste in an effective approach. In this study, chemically modified spent coffee husk (CH) has [...] Read more.
Waste biomass-based natural fibers are being extensively researched nowadays as a composite material with various waste-based high-density polyethylene (HDPE) to utilize the waste biomass and recycle the plastic waste in an effective approach. In this study, chemically modified spent coffee husk (CH) has been applied with different ratios of HDPE to produce composite material and characterized comprehensively to determine the mechanical stability of the products. The injection molding method was used for composite development containing HDPE with untreated and 10 wt% NaOH-treated CH weight ratios of 0%, 15%, 20%, and 25% together with 10 wt% coupling agent and filler materials of acrylonitrile butadiene styrene (ABS) and kaolin clay, respectively. Physicochemical characteristics of untreated CH, 10 wt% NaOH treated CH, pristine HDPE and HDPE-CH composites have been analyzed comprehensively in this study. Adding 25 wt% fiber with 65 wt% HDPE and 10 wt% of ABS (7 wt%)-kaolin clay (3 wt%) increased the tensile and bending properties significantly. This composite presented the maximum tensile, flexural, and impact strengths, which were 36 MPa, 7.5 MPa, and 2.8 KJ/m2, respectively. The tensile strength and bending strength of NaOH-treated coffee husk fibers (CHF) were enhanced by 32% and 29%, respectively. The microstructural characteristics of HDPE with treated and untreated CHF composites analyzed by scanning electron microscopy (SEM) demonstrated the fibers’ and matrix’s excellent adhesion and compatibility. Thus, HDPE polymer-treated CH composite presented excellent stability, which can be expected as a new addition for construction, food packaging, and other industrial applications. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Representation of the processing sequence to produce UC and TC composites with their characterization.</p>
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<p>Tensile strength test results. UT15, UT20, UT25, T15, T20, and T25 represent 15% of untreated CH, 20% of untreated CH, 25% of untreated CH, 15% of treated CH, 20% of untreated CH and 25% of untreated CH in the composite mixtures, respectively.</p>
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<p>Tensile force-elongation diagram of treated and untreated CH composites. Here, 65% TT, 65% UTT, 70% UTT, 70% TT, 75% TT and 75% UTT represent 65% of treated CH, 65% of untreated CH, 70% of untreated CH, 70% of treated CH, 75% of untreated CH and 75% of treated CH in the composite mixtures, respectively.</p>
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<p>Flexural strength results.</p>
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<p>Impact strength test results of CH composite.</p>
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<p>Moisture absorption test results of CH composites.</p>
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<p>SEM image of (<b>A</b>) 75 wt% treated, (<b>B</b>) 65 wt% treated, (<b>C</b>) 75 wt% untreated, and (<b>D</b>) 65 wt% untreated CH composites.</p>
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<p>Diffraction of X-rays of NaOH-treated composites.</p>
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<p>Diffraction of X-rays of untreated composites.</p>
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22 pages, 4663 KiB  
Article
Influence of Spatially Distributed Out-of-Plane CFRP Fiber Waviness on the Estimation of Knock-Down Factors Based on Stochastic Numerical Analysis
by Andreas Schuster, Richard Degenhardt, Christian Willberg and Tobias Wille
J. Compos. Sci. 2022, 6(12), 353; https://doi.org/10.3390/jcs6120353 - 22 Nov 2022
Cited by 1 | Viewed by 1598
Abstract
The presence of waviness defects in CFRP materials due to fiber undulation affects the structural performance of composite structures. Hence, without a reliable assessment of the resulting material properties, the full weight-saving potential cannot be exploited. Within the paper, a probabilistic numerical approach [...] Read more.
The presence of waviness defects in CFRP materials due to fiber undulation affects the structural performance of composite structures. Hence, without a reliable assessment of the resulting material properties, the full weight-saving potential cannot be exploited. Within the paper, a probabilistic numerical approach for improved estimation of material properties based on spatially distributed fiber waviness is presented. It makes use of a homogenization approach to derive viable knock-down factors for the different plies on the laminate level for reference material and is demonstrated for a representative tension loadcase. For the stochastic analysis, a random field is selected which describes the complex inner geometry of the plies in the laminate model and is numerically discretized by the Karhunen–Loeve expansion methods to fit into an FE model for the strength analysis. Conducted analysis studies reveal a substantial influence of randomly distributed waviness defects on the derived knock-down factors. Based on a topological analysis of the waviness fields, the reduction of the material properties was found to be weakly negatively correlated related to simple geometrical properties such as maximum amplitudes of the waviness field, which justifies the need for further subsequent sensitivity studies. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Two-dimensional examples of out-of-plane fiber waviness in a composite laminate. (<b>a</b>) Embedded single graded waviness, reprinted with permission from Ref. [<a href="#B5-jcs-06-00353" class="html-bibr">5</a>], 2013, S. Mukhopadhyay; (<b>b</b>) hump, reprinted with permission from Ref. [<a href="#B6-jcs-06-00353" class="html-bibr">6</a>], 2012, P. Davidson; (<b>c</b>) complex stochastic distributed waviness, reprinted with permission from Ref. [<a href="#B7-jcs-06-00353" class="html-bibr">7</a>], 2010, R. Hinterhölzl.</p>
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<p>Illustration of homogenization approach for KDF parameter estimation based on pristine (left) and defective model configuration (right), reprinted with permission from Ref. [<a href="#B29-jcs-06-00353" class="html-bibr">29</a>], 2020, F. Heinecke).</p>
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<p>Exemplary Matern-kernel functions for the different realization of the parameter <math display="inline"><semantics> <mi>ν</mi> </semantics></math>.</p>
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<p>KLE-based waviness modeling of a generic CFRP cross-section made up of 8 layers for three different numbers of eigenvalues. The numerical approximated random field is highlighted in red. (<b>a</b>) 6 modes; (<b>b</b>) 12 modes; (<b>c</b>) 20 modes.</p>
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<p>Simplified workflow for the estimation of stochastic knock-down factors.</p>
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<p>Two examples of random field realizations embedded in a reference FE model for a laminate of the thickness <math display="inline"><semantics> <msub> <mi>t</mi> <mrow> <mi>l</mi> <mi>a</mi> <mi>m</mi> </mrow> </msub> </semantics></math> with about 169,000 degrees of freedom. The upper half layers of the laminate are made transparent for visibility. The color indicates the relative displacements of the ply with respect to a nominal pristine position.</p>
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<p>Node sets at model boundary and applied loads for tensile loadcase. (Reprinted with permission from Ref. [<a href="#B29-jcs-06-00353" class="html-bibr">29</a>], 2020, F. Heinecke).</p>
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<p>(<b>a</b>) KDF plot of deterministic analysis for <math display="inline"><semantics> <msub> <mi>R</mi> <mi>x</mi> </msub> </semantics></math> loadcase; (<b>b</b>) random field example used for deterministic analysis.</p>
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<p>Convergence of KDF according to mesh refinement in the x-direction.</p>
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<p>Convergence of KDF according to mesh refinement in the z-direction (layer thickness direction).</p>
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<p>Distribution of mean of KDF for <math display="inline"><semantics> <msub> <mi>R</mi> <mi>x</mi> </msub> </semantics></math> within the selected laminate configuration with related variances as second bar element of the stochastic results. For each layer, the ply angle is additionally printed.</p>
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<p>Distribution of KDF histograms for <math display="inline"><semantics> <msub> <mi>R</mi> <mi>x</mi> </msub> </semantics></math> at specific layers within selected laminate configuration.</p>
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<p>Scatter plot of waviness ratio compared to resulting KDF for property <math display="inline"><semantics> <msub> <mi>R</mi> <mi>x</mi> </msub> </semantics></math>. Plies that share the same fiber orientation angle are colored equally.</p>
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<p>Selection of three exemplary random fields with a similar waviness ratio at the midsurface of the laminate.</p>
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<p>Correlation coefficients for tensile KDF related to waviness ratio.</p>
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<p>Scatter plot of maximum curvature in fiber orientation direction compared to resulting KDF for <math display="inline"><semantics> <msub> <mi>R</mi> <mi>x</mi> </msub> </semantics></math>. Plies that share the same fiber orientation angle are colored equally.</p>
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<p>Correlation coefficient for tensile KDF related to fiber orientation aligned maximum curvature.</p>
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16 pages, 5475 KiB  
Article
Utilizing of Magnetized Water in Enhancing of Volcanic Concrete Characteristics
by Mostafa M. Keshta, Mohamed M. Yousry Elshikh, Mohamed Abd Elrahman and Osama Youssf
J. Compos. Sci. 2022, 6(10), 320; https://doi.org/10.3390/jcs6100320 - 19 Oct 2022
Cited by 19 | Viewed by 2841
Abstract
Volcanic concrete is an eco-friendly concrete type in that it contains coarse and fine aggregates that all extracted from the igneous volcanic rock. However, utilizing of volcanic ash (VA) as partial/full replacement of concrete cement significantly affects the concrete workability, especially at high [...] Read more.
Volcanic concrete is an eco-friendly concrete type in that it contains coarse and fine aggregates that all extracted from the igneous volcanic rock. However, utilizing of volcanic ash (VA) as partial/full replacement of concrete cement significantly affects the concrete workability, especially at high cement replacement ratios. This has also some adverse effects on concrete strength. Utilizing magnetized water (MW) in concrete as a partial/full replacement of ordinary tap water (TW) has a notable effect on enhancing the fresh and hardened concrete properties. This research aims to study the effect of using MW prepared in a magnetic field of 1.4 Tesla on the workability and hardened properties (compressive, tensile, and flexural strengths) of volcanic concrete. In this study, VA partially replaced volcanic concrete cement with ratios of 5%, 10%, 15%, and 20%. Ten volcanic concrete mixes were prepared in two groups. The first one was prepared with VA (0–20%) and mixed with TW. The other group was prepared with the same VA contents like group one, but mixed with MW. Microstructure imaging for volcanic concrete was also conducted in this study. Results of water tests showed 17% and 15% increase in total dissolved solids (TDS) and pH, respectively, of MW compared with those of TW. In addition, the water magnetization decreased the water surface tension by 7% compared with that of TW. Results of hardened concrete tests showed that the best ratio of VA in volcanic concrete was 5% with and without using magnetized water. The volcanic concrete slump decreased when using TW; however, using MW enhanced the volcanic concrete slump by up to 8%. The compressive strength was improved by 35%, 23%, and 20% at 7 days, 28 days, and 120 days, respectively, with no VA and with the presence of MW. The compressive strength was improved by 11%, 12%, and 11% after 7 days, 28 days, and 120 days, respectively, with using 5% VA and with the presence of MW. Both splitting tensile strength and flexural strength of volcanic concrete with and without VA or MW behaved similar to that of the corresponding compressive strength. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Water molecules after magnetization [<a href="#B29-jcs-06-00320" class="html-bibr">29</a>].</p>
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<p>Volcanic rocks as coarse aggregate, fine aggregate, and volcanic ash.</p>
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<p>EDX analysis of VA.</p>
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<p>TGA analysis of VA.</p>
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<p>Permanent magnet utilized in magnetizing the water.</p>
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<p>SEM image of VA particles.</p>
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<p>Effect of VA ratio on the slump of volcanic concrete made with tap water.</p>
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<p>Effect of magnetized water on volcanic concrete slump.</p>
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<p>Effect of different ratios of VA on volcanic concrete compressive strength mixed with tap water.</p>
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<p>SEM images of the fracture surface of volcanic concrete made with TW: (<b>a</b>) 0%VA and (<b>b</b>) 5% VA.</p>
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<p>Effect of MW on compressive strength of volcanic concrete at 7, 28, and 120 days.</p>
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<p>SEM images of the fracture surface of volcanic concrete made with MW: (<b>a</b>) 0%VA and (<b>b</b>) 5% VA.</p>
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<p>Volcanic concrete splitting tensile strength: (<b>a</b>) effect of VA and (<b>b</b>) effect of MW.</p>
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<p>Volcanic concrete flexural strength: (<b>a</b>) effect of VA and (<b>b</b>) effect of MW.</p>
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13 pages, 3517 KiB  
Article
Mixed-Mode I/II Testing of Composite Materials—A Refined Data Reduction Scheme for the Wedge-Loaded Asymmetric Double Cantilever Beam Test
by Michael May, Philipp Hahn, Borhan Uddin Manam and Mathieu Imbert
J. Compos. Sci. 2022, 6(10), 319; https://doi.org/10.3390/jcs6100319 - 18 Oct 2022
Cited by 6 | Viewed by 2655
Abstract
The wedge-loaded asymmetric double cantilever beam (WADCB) test is an experimental method to determine the mixed-mode I/II fracture toughness of composite materials by inserting a wedge into the specimen along a potential delamination path. Whilst the current closed-form solution for the ADCB test [...] Read more.
The wedge-loaded asymmetric double cantilever beam (WADCB) test is an experimental method to determine the mixed-mode I/II fracture toughness of composite materials by inserting a wedge into the specimen along a potential delamination path. Whilst the current closed-form solution for the ADCB test assumes identical forces acting in both specimen arms, this manuscript proposes a refined closed-form solution allowing for different forces acting on both specimen arms, which is thought to be more general and more rigorous. WADCB tests were carried out on composites made from Torayca T700SC/2592 unidirectional prepreg. Both the current and the refined closed-form solution were used to analyze the data, and some differences were found in the predictions, indicating that the forces in the two specimen arms are indeed not identical. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>WDCB test setup with “floating” wedge.</p>
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<p>Schematic of the WADCB test.</p>
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<p>WADCB test for thickness ratio 0.25. Top: global view; Bottom: close-up view of the delamination area.</p>
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<p>WADCB test for thickness ratio 0.48. Top: global view; Bottom: close-up view of the delamination area.</p>
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<p>WADCB test for thickness ratio 0.74. Top: global view; Bottom: close-up view of the delamination area.</p>
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10 pages, 1935 KiB  
Article
Threshold Identification and Damage Characterization of Woven GF/CF Composites under Low-Velocity Impact
by Marzio Grasso and Yigeng Xu
J. Compos. Sci. 2022, 6(10), 305; https://doi.org/10.3390/jcs6100305 - 11 Oct 2022
Cited by 3 | Viewed by 1905
Abstract
The Delamination Threshold Load (DTL) is a key parameter representing damage resistance of a laminate and is normally identified by locating a sudden drop in the impact force-time history for the laminate made of unidirectional layers. For the woven composite, however, their failure [...] Read more.
The Delamination Threshold Load (DTL) is a key parameter representing damage resistance of a laminate and is normally identified by locating a sudden drop in the impact force-time history for the laminate made of unidirectional layers. For the woven composite, however, their failure mechanisms appear different and the current literature is not providing any clear procedure regarding the identification of the delamination initiation, as well as the evolution of the failure mechanisms associated with it. In this paper, experimental data have been collected using woven glass and carbon fiber composites. The results are analyzed in terms of force-time and force-displacement curves. While delamination and other damages were clearly observed using ultrasonic scans, the analysis of the results does not reveal any trend changes of the curves that can be associated with the incipient nucleation of delamination. A preliminary discussion regarding the nature of the mechanisms through which the delamination propagates in woven composite and a justification for the absence of a sudden change of the stiffness have been presented. It raises a question on the existence of DTL for woven composites under low velocity impact. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Damage characterisation B-Scans—Carbon Fibre—5 J to 30 J (<b>a</b>–<b>f</b>).</p>
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<p>Damage characterization B-Scans—Glass Fiber—5 J to 30 J (<b>a</b>–<b>f</b>).</p>
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<p>Force time history for Carbon (<b>left</b>) and Glass (<b>right</b>) fibers tested.</p>
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<p>Comparison between the as acquired and low pass filtered curves.</p>
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<p>Force displacement curves for carbon fibers (<b>left</b>) and glass fibers (<b>right</b>).</p>
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<p>Energy profile with the equal energy curve.</p>
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<p>Peak force as a function of the impact energy for the carbon fibers (black) and glass fibers (green).</p>
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16 pages, 6694 KiB  
Article
Mitigation of Heat Propagation in a Battery Pack by Interstitial Graphite Nanoplatelet Layer: Coupled Electrochemical-Heat Transfer Model
by Barbara Palmieri, Fabrizia Cilento, Ciro Siviello, Francesco Bertocchi, Michele Giordano and Alfonso Martone
J. Compos. Sci. 2022, 6(10), 296; https://doi.org/10.3390/jcs6100296 - 9 Oct 2022
Cited by 10 | Viewed by 2599
Abstract
The use of high thermal conductive materials for heat transfer is gaining attention as a suitable treatment for improving battery performance. Thermal runaway is a relevant issue for maintaining safety and for proficient employment of accumulators; therefore, new solutions for thermal management are [...] Read more.
The use of high thermal conductive materials for heat transfer is gaining attention as a suitable treatment for improving battery performance. Thermal runaway is a relevant issue for maintaining safety and for proficient employment of accumulators; therefore, new solutions for thermal management are mandatory. For this purpose, a hierarchical nanomaterial made of graphite nanoplatelet has been considered as an interface material. High-content graphite nanoplatelet films have very high thermal conductivity and might improve heat dissipation. This study investigates the effect of a thermally conductive material as a method for safety enhancement for a battery module. A numerical model based on the finite element method has been developed to predict the heat generation during a battery pack’s charge and discharge cycle, using the Multiphysics software Comsol. The lumped battery interface generates appropriate heat sources coupled to the Heat Transfer Interface in 3D geometry. Simulation results show that the protection of neighbouring cells from the interleaved layer is fundamental for avoiding heat propagation and an uncontrollable heating rise of the entire battery pack. The use of graphite nanocomposite sheets could effectively help to uniform the temperature and delay the TR propagation. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Critical stages that lead to the occurrence of the TR phenomenon.</p>
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<p>Scheme of the battery pack.</p>
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<p>Charge-discharge cycle applied at the battery.</p>
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<p>Curves of <span class="html-italic">E<sub>OCV</sub></span> vs. <span class="html-italic">SOC</span> at the reference temperature and of the <span class="html-italic">SOC</span> derivative with respect to the reference temperature vs. the <span class="html-italic">SOC</span>.</p>
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<p>Model mesh realised.</p>
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<p>Triggered battery with a T<sub>in</sub> of 130 °C: (<b>a</b>) without GNP layer; (<b>b</b>) with GNP layer.</p>
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<p>(<b>a</b>) Change in current and voltage during the discharge–charge cycle of batteries; (<b>b</b>) temperature rise vs. applied current.</p>
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<p>Temperature distribution inside the battery pack at different instants of time: (<b>a</b>) t = 0 s; (<b>b</b>) t = 500 s; (<b>c</b>) t = 1000 s and (<b>d</b>) t = 1500 s.</p>
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<p>(<b>a</b>) Curve of reaction rate vs. temperature (Equation (9)); (<b>b</b>) heat generation by decomposition reactions (Equation (10)).</p>
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<p>Temperature distribution inside the battery pack as a result of the decomposition reactions: (<b>a</b>) instant t = 0; (<b>b</b>) t = 500 s; (<b>c</b>) t = 1000 s and (<b>d</b>) t = 1500 s.</p>
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<p>Temperature vs. time prediction; the model includes the TR kinetic. The inset picture reproduces the experimental temperature trend when TR is incipient, adapted from [<a href="#B34-jcs-06-00296" class="html-bibr">34</a>].</p>
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<p>Temperature distribution inside the battery pack after 1500 s: (<b>a</b>) no thermal conductive layer; (<b>b</b>) by considering the GNP layer as heat spreader with the ambient.</p>
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<p>Thermal distribution in plane and cross-plane of the GNP layer.</p>
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<p>(<b>a</b>) Temperature rises inside the batteries vs. applied current for the model with the GNP as heat spreader; (<b>b</b>) temperature distribution inside the GNP layer.</p>
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<p>(<b>a</b>) Temperature distribution inside the battery pack without the heat spreader; (<b>b</b>) temperature distribution inside the battery pack with the heat spreader.</p>
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<p>(<b>a</b>) Temperature distribution inside the battery pack without the heat spreader; (<b>b</b>) temperature distribution inside the battery pack with the heat spreader.</p>
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<p>Maximum temperature curve vs. time, for the case with and without the heat spreader.</p>
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10 pages, 3231 KiB  
Article
A Study on the Structural Features of Amorphous Nanoparticles of Ni by Molecular Dynamics Simulation
by Tuan Tran Quoc, Dung Nguyen Trong, Van Cao Long, Umut Saraç and Ştefan Ţălu
J. Compos. Sci. 2022, 6(9), 278; https://doi.org/10.3390/jcs6090278 - 19 Sep 2022
Cited by 3 | Viewed by 1895
Abstract
This study deals with the impact of the heating rate (HR), temperature (T), and the number of atoms (N) on the structural features of amorphous nanoparticles (ANPs) of Ni by molecular dynamics simulation (MDS) with the Pak–Doyama pair interaction potential field (PD). The [...] Read more.
This study deals with the impact of the heating rate (HR), temperature (T), and the number of atoms (N) on the structural features of amorphous nanoparticles (ANPs) of Ni by molecular dynamics simulation (MDS) with the Pak–Doyama pair interaction potential field (PD). The obtained results showed that the structural features of ANPs of Ni are significantly affected by the studied factors. The correlation between the size (D) and the N was determined to be D~N−1/3. The energy (E) was proportional to N−1, and the Ni-Ni link length was 2.55 Å. The glass transition temperature (Tg) derived from the E-T graph was estimated to be 630 K. An increase in the HR induced a change in the shape of the ANPs of Ni. Furthermore, raising the HR caused an enhancement in the D and a decrement in the density of atoms. The obtained results are expected to contribute to future empirical studies. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>The shape (<b>a</b>), CNs (<b>b</b>), and RDF (<b>c</b>) of Ni<sub>5324</sub> ANPs with heating rate of 10<sup>6</sup> K/s at T = 300 K.</p>
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<p>The shape (<b>a1</b>–<b>a6</b>), CNs (<b>b1</b>–<b>b6</b>), and RDF (<b>c1</b>–<b>c6</b>) of ANPs of Ni<sub>5324</sub> with different HRs.</p>
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<p>The shape (<b>a1</b>–<b>a6</b>), CNs (<b>b1</b>–<b>b6</b>), and RDF (<b>c1</b>–<b>c6</b>) of ANPs of Ni<sub>5324</sub> with different HRs.</p>
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<p>The shape (<b>a</b>), RDF (<b>b</b>), and CN (<b>c</b>) of the ANPs of Ni<sub>2048</sub> with respect to the N.</p>
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<p>The correlation between the D and the N (<b>a</b>), and the correlation between the E and the N (<b>b</b>) of amorphous Ni materials with different number of atoms.</p>
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<p>The shape (<b>a</b>), RDF (<b>b</b>), and CN (<b>c</b>) of the ANPs of Ni<sub>5324</sub> with respect to T.</p>
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<p>The T<sub>g</sub> of the ANPs of Ni<sub>5324</sub>.</p>
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13 pages, 3726 KiB  
Article
Finite Element Simulation of FRP-Strengthened Thin RC Slabs
by Maha Assad, Rami Hawileh and Jamal Abdalla
J. Compos. Sci. 2022, 6(9), 263; https://doi.org/10.3390/jcs6090263 - 8 Sep 2022
Cited by 13 | Viewed by 2263
Abstract
This study aims to investigate the flexural behavior of high-strength thin slabs externally strengthened with fiber-reinforced polymer (FRP) laminates through a numerical simulation. A three-dimensional (3D) finite element (FE) model is created to simulate the response of strengthened reinforced concrete (RC) slabs under [...] Read more.
This study aims to investigate the flexural behavior of high-strength thin slabs externally strengthened with fiber-reinforced polymer (FRP) laminates through a numerical simulation. A three-dimensional (3D) finite element (FE) model is created to simulate the response of strengthened reinforced concrete (RC) slabs under a four-point bending test. The numerical model results in terms of load-deflection behavior, and ultimate loads are verified using previously published experimental data in the literature. The numerical results show a good agreement with the experimental results. The FE model is then employed in a parametric study to inspect the effect of concrete compressive strength on the performance of RC thin slabs strengthened with different FRP types, namely carbon fiber-reinforced polymers (CFRP), polyethylene terephthalate fiber-reinforced polymers (PET-FRP), basalt fiber-reinforced polymers (BFRP) and glass fiber-reinforced polymers (GFRP). The results showed that the highest strength enhancement was obtained by the slab that was strengthened by CFRP sheets. Slabs that were strengthened with other types of FRP sheets showed an almost similar flexural capacity. The effect of concrete compressive strength on the flexural behavior of the strengthened slabs was moderate, with the highest effect being a 15% increase in the ultimate load between two consecutive values of compressive strength, occurring in the CFRP-strengthened slabs. It can thus be concluded that the developed FE model could be used as a platform to predict the behavior of reinforced concrete slabs when strengthened with different types of FRP composites. It can also be concluded that the modulus of elasticity of the composite plays a major role in determining the flexural capacity of the strengthened slabs. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Geometrical configuration and test setup of the tested slab: (<b>a</b>) Elevation and location of loading; (<b>b</b>) Cross section of the slab.</p>
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<p>Developed FE model components in ANSYS: (<b>a</b>) 3D view; (<b>b</b>) boundary conditions; (<b>c</b>) bottom view.</p>
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<p>Bond-slip model used to simulate interfacial behavior between FRP and concrete.</p>
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<p>Constitutive models for concrete with <span class="html-italic">f′<sub>c</sub></span> of 70 MPa: (<b>a</b>) Compressive stress-strain curve; (<b>b</b>) tensile stress-strain curve.</p>
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<p>Load-deflection curves from FE model and experimental test [<a href="#B10-jcs-06-00263" class="html-bibr">10</a>]: (<b>a</b>) Control slab; (<b>b</b>) C1; (<b>c</b>) C2.</p>
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<p>Load-deflection curves from FE model and experimental test [<a href="#B10-jcs-06-00263" class="html-bibr">10</a>]: (<b>a</b>) Control slab; (<b>b</b>) C1; (<b>c</b>) C2.</p>
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<p>Failure mode of a slab specimen strengthened with one CFRP layer: (<b>a</b>) Experiment [<a href="#B10-jcs-06-00263" class="html-bibr">10</a>]; (<b>b</b>) FE model.</p>
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<p>Effect of FRP type on the load-deflection behavior of a strengthened slab specimen.</p>
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<p>Effect of concrete compressive strength on the behavior of CFRP-strengthened slabs.</p>
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<p>Effect of concrete compressive strength on the behavior of GFRP-strengthened slabs.</p>
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<p>Effect of concrete compressive strength on the behavior of BFRP-strengthened slabs.</p>
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<p>Effect of concrete compressive strength on the behavior of PET-FRP-strengthened slabs.</p>
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15 pages, 6263 KiB  
Article
Experimental and Finite Element Study of a Novel Two-Way Corrugated Steel Deck System for Composite Slabs
by Keerthana John, Mahmud Ashraf, Matthias Weiss and Riyadh Al-Ameri
J. Compos. Sci. 2022, 6(9), 261; https://doi.org/10.3390/jcs6090261 - 8 Sep 2022
Cited by 4 | Viewed by 2380
Abstract
This paper investigates the structural performance of a new two-way profiled steel decking system for steel-concrete composite slabs. Several studies have investigated steel decking for steel-concrete composite slabs and focused on utilising the conventional deck as a one-way floor system. The newly developed [...] Read more.
This paper investigates the structural performance of a new two-way profiled steel decking system for steel-concrete composite slabs. Several studies have investigated steel decking for steel-concrete composite slabs and focused on utilising the conventional deck as a one-way floor system. The newly developed deck consists of top-hat sections formed by bending corrugated sheets at 90°, which are attached to a corrugated base sheet. The deck is designed for improved composite and two-way action contributed by its unique geometry due to corrugations in the transverse and longitudinal directions. This paper experimentally tested a novel steel decking geometry under construction stage loading. It was in the absence of concrete to establish the deck’s suitability for construction and contribution towards loading capacity and performance for future use as a two-way composite slab. Ultimate load, two-way action, and failure modes were identified. A finite element model was also developed, and parameters assessed that could influence the performance when the deck is potentially used in the composite stage. It was concluded that, while increasing the thickness of the corrugated base sheet significantly affects the load-carrying capacity, the thickness of the top hats has no significant impact. Improved load transfer with two-way behaviour is observed when the bottom flanges of the top hats are continuously connected to the bottom flanges of the adjacent top hats to form a deck. This contrasts with the concept deck, where individual top hats are attached to a corrugated base sheet. In this case, decks with a corrugated base sheet perform 54% better in ultimate load capacity than decks without a corrugated base sheet. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Two-way steel deck system. (<b>a</b>) Cross-section dimensions of two-way deck system. (<b>b</b>) Corrugated top-hat rib section. (<b>c</b>) Assembled two-way deck. (<b>d</b>) Mechanism of shear bond in new deck profile.</p>
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<p>Test setup. (<b>a</b>) Experimental setup and loading. (<b>b</b>) Schematic of the test setup. (<b>c</b>) Strain gauge positions.</p>
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<p>Failure modes of two-way deck system. (<b>a</b>) Failed deck with deformed top-hats. (<b>b</b>) Local deformations seen on a corrugated base sheet at supported points. (<b>c</b>) Minor local deformations on the corrugated base sheet at ultimate load.</p>
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<p>Load-displacement curves.</p>
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<p>Load-strain curves (<b>a</b>) D1 sample, (<b>b</b>) D2 sample.</p>
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<p>Symmetric FE model of the tested two-way deck.</p>
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<p>Mesh convergence study of the two-way deck.</p>
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<p>Validation of FE model results. (<b>a</b>) Load-displacement comparison of experimental result and FE result. (<b>b</b>) Failure mode comparison of the experimental deck and FE deck model.</p>
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<p>Load–displacement curves for decks of varying thickness of the corrugated base sheet.</p>
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<p>Load–displacement curves for decks of varying thickness of top-hat ribs.</p>
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<p>Continuous bottom flanges of top hats placed on a corrugated base sheet.</p>
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<p>Load–displacement curve comparison for decks with connected bottom flanges of top-hat ribs.</p>
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<p>Failed CTH-BS deck with high stress along base sheet indicating higher load distribution along the weak direction.</p>
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<p>(<b>a</b>) Load-displacement curve comparison for decks of connected bottom flanges of top-hat ribs in the absence of corrugated base sheet, (<b>b</b>) Percentage load distributed along each direction of the deck through the entire loading stage.</p>
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<p>Failure of CTH deck type.</p>
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22 pages, 4853 KiB  
Article
Development and Characterization of PHB-PLA/Corncob Composite for Fused Filament Fabrication
by Okezie Ohaeri and Duncan Cree
J. Compos. Sci. 2022, 6(9), 249; https://doi.org/10.3390/jcs6090249 - 26 Aug 2022
Cited by 11 | Viewed by 2787
Abstract
The development of environmentally friendly polymeric composites holds great potential for agricultural leftovers. This study explores the effects of lignocellulosic corncob powder as a filler in a polyhydroxybutyrate (PHB)/polylactic acid (PLA) biopolymer matrix. The PHB-PLA matrix consists of a 55% to 45% blend, [...] Read more.
The development of environmentally friendly polymeric composites holds great potential for agricultural leftovers. This study explores the effects of lignocellulosic corncob powder as a filler in a polyhydroxybutyrate (PHB)/polylactic acid (PLA) biopolymer matrix. The PHB-PLA matrix consists of a 55% to 45% blend, respectively, while the filler loadings range from 0 wt.% to 8 wt.%. The components are combined and directly extruded into fused filaments for three-dimensional (3D) printing. The tensile strength of both the filament and dog-bone samples, flexural strength, and Charpy impact toughness of the composites, all decreased as filler loading increased. The tensile and flexural modulus of all samples examined improved noticeably with increasing filler loading. The filler particles had dense, mildly elongated sheet-like shapes, whereas the fractured surfaces of the composite samples had flat features for the pure polymer blend, but became rougher and jagged as filler loading increased. The fractured surface of Charpy impact test samples had smoother morphology when tested at cryogenic temperatures, compared to room temperature testing. All attributes showed a fourth-degree polynomial relationship to filler loading and all improved as filler loading increased, with the best results obtained at 6 wt.% loading. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Filament extrusion apparatus: (<b>a</b>) Filabot spooler; and (<b>b</b>) Filabot extruder.</p>
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<p>Typical 3D printed tensile test specimens: (<b>A</b>) Pure PHB/PLA with 0 wt.% corncob; (<b>B</b>) 2 wt.% corncob; (<b>C</b>) 4 wt.% corncob; (<b>D</b>) 6 wt.% corncob; and (<b>E</b>) 8 wt.% corncob.</p>
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<p>Scanning electron micrograph showing particle morphology of corncob powder (20 µm sieve): (<b>a</b>) At low magnification; and (<b>b</b>) At higher magnification.</p>
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<p>Effect of filler loading on the fused filaments: (<b>a</b>) Tensile strength; and (<b>b</b>) Tensile modulus.</p>
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<p>SEM micrographs of tensile tested fused filaments fractured surfaces: (<b>A</b>) denotes PHB (55%)/PLA (45%); (<b>B</b>) denotes PHB (55%)/PLA (45%) + 2 wt.% CC; (<b>C</b>) denotes PHB (55%)/PLA (45%) + 4 wt.% CC; (<b>D</b>) denotes PHB (55%)/PLA (45%) + 6 wt. % CC; (<b>E</b>) denotes PHB (55%)/PLA (45%) + 8 wt.% CC. Micrographs (<b>E</b>–<b>J</b>) are magnified images of the regions denoted by circles in micrographs A to E, respectively.</p>
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<p>Effect of filler loadings on the 3D printed specimen: (<b>a</b>) Tensile strength; (<b>b</b>) Tensile modulus; and (<b>c</b>) Percentage elongation.</p>
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<p>SEM micrographs of tensile test 3D printed test specimen fractured surfaces: (<b>A</b>) Denotes PHB (55%)/PLA (45%); (<b>B</b>) Denotes PHB (55%)/PLA (45%) + 2 wt.% CC; (<b>C</b>) Denotes PHB (55%)/PLA (45%) + 4 wt.% CC; (<b>D</b>) Denotes PHB (55%)/PLA (45%) + 6 wt.% CC; (<b>E</b>) Denotes PHB (55%)/PLA (4 5%) + 8 wt.% CC.</p>
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<p>Effect of filler loadings on the 3D printed specimen: (<b>a</b>) Flexural strength; and (<b>b</b>) Flexural modulus.</p>
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<p>SEM micrographs of flexural test 3D printed test specimen fractured surfaces: (<b>A</b>) Denotes PHB (55%)/PLA (45%); (<b>B</b>) Denotes PHB (55%)/PLA (45%) + 2 wt.% CC; (<b>C</b>) Denotes PHB (55%)/PLA (45%) + 4 wt.% CC; (<b>D</b>) Denotes PHB (55%)/PLA (45%) + 6 wt.% CC; (<b>E</b>) Denotes PHB (55%)/PLA(45%) + 8 wt.% CC.</p>
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<p>Effect of filler loadings on the Charpy impact energy of the 3D printed specimens at: (<b>a</b>) 22 °C; and (<b>b</b>) −38 °C.</p>
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<p>SEM micrographs of Charpy impact 3D printed test specimen fractured surfaces at 22 °C: (<b>A</b>) Denotes PHB (55%)/PLA (45%); (<b>B</b>) Denotes PHB (55%)/PLA (45%) + 2 wt.% CC; (<b>C</b>) Denotes PHB (55%)/PLA (45%) + 4 wt.% CC; (<b>D</b>) Denotes PHB (55%)/PLA (45%) + 6 wt.% CC; (<b>E</b>) Denotes PHB (55%)/PLA (45%) + 8 wt.% CC.</p>
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<p>SEM micrographs of Charpy impact 3D printed test specimen fractured surfaces at −38 °C: (<b>A</b>) Denotes PHB (55%)/PLA (45%); (<b>B</b>) Denotes PHB (55%)/PLA (4 5%) + 2 wt.% CC; (<b>C</b>) Denotes PHB (55%)/PLA (45%) + 4 wt.% CC; (<b>D</b>) Denotes PHB (55%)/PLA (45%) + 6 wt.% CC; (<b>E</b>) Denotes PHB (55%)/PLA (45%) + 8 wt.% CC.</p>
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<p>A DSC thermograph showing the effect of corncob fillers on the T<sub>g</sub> and melt peaks of the composites.</p>
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<p>Effect of filler loading on water absorption of PHB/PLA corncob composites.</p>
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17 pages, 56661 KiB  
Article
Prediction of Damage in Non-Crimp Fabric Composites Subjected to Transverse Crushing: A Comparison of Two Constitutive Models
by Milad Kazemian and Aleksandr Cherniaev
J. Compos. Sci. 2022, 6(8), 224; https://doi.org/10.3390/jcs6080224 - 4 Aug 2022
Cited by 1 | Viewed by 2734
Abstract
Non-crimp fabrics (NCFs) are increasingly used in industry for manufacturing of composite structures due to a combination of high mechanical properties and excellent manufacturability. As with other composites, in-service damage can be a cause for severe reduction in load-carrying capacity of NCF-reinforced plastics. [...] Read more.
Non-crimp fabrics (NCFs) are increasingly used in industry for manufacturing of composite structures due to a combination of high mechanical properties and excellent manufacturability. As with other composites, in-service damage can be a cause for severe reduction in load-carrying capacity of NCF-reinforced plastics. In this experimental and numerical study, two constitutive material models previously used only for damage prediction in unidirectional (UD) tape and woven fabric-reinforced materials (LS-DYNA’s *MAT_ENHANCED_COMPOSITE_DAMAGE—MAT54 and *MAT_LAMINATED_COMPOSITE_FABRIC—MAT58) were evaluated for simulating transverse crushing of composite parts processed from a non-crimp carbon fabric. For this purpose, UD NCF components of tubular shape were subjected to transverse crushing through a controlled indentation of a metallic cylinder, and results of the experiment were compared with numerical modeling. Considered verification metrics included the observed and the predicted patterns of interlaminar damage, the extent of delamination, as well as the ability of the models to replicate force-displacement response exhibited by the tested specimens. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Non-crimp unidirectional carbon fabric.</p>
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<p>Manufacturing of NCF components: the molds and the processed parts.</p>
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<p>Test setup for material characterization experiments.</p>
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<p>Stress–strain diagrams for the NCF material.</p>
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<p>Transverse crushing of the tubular NCF specimen.</p>
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<p>Image of the crushed <math display="inline"><semantics> <mrow> <msub> <mrow> <mfenced close="]" open="["> <mrow> <msub> <mn>0</mn> <mn>4</mn> </msub> <mo>,</mo> <msub> <mrow> <mn>90</mn> </mrow> <mn>3</mn> </msub> </mrow> </mfenced> </mrow> <mi mathvariant="normal">S</mi> </msub> </mrow> </semantics></math> specimen obtained using X-ray computed tomography.</p>
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<p>Developed LS-DYNA numerical model (the quarter-model reflected to enhance representation).</p>
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<p>Visual and predicted (MAT54) damage in the outer layer of the [0<sub>4</sub>, 90<sub>3</sub>]<sub>S</sub> specimen (color scheme: gray—not damaged, red—fully damaged; indenter shown for scale representation only).</p>
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<p>MAT58 predicted damage in the outer layer of the [0<sub>4</sub>, 90<sub>3</sub>]<sub>S</sub> specimen (color scheme: gray—not damaged, red—fully damaged; indenter shown for scale representation only).</p>
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<p>Delamination in the central 100 mm-long segment of the crushed [0<sub>4</sub>, 90<sub>3</sub>]<sub>S</sub> specimen: CT-scan vs. numerical modeling. (<b>a</b>) X-ray computed tomography; (<b>b</b>) MAT54 model: delamination (overlayed images); (<b>c</b>) MAT58 model: delamination (overlayed images).</p>
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<p>Force–displacement diagrams: experiment vs. numerical modeling.</p>
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Review

Jump to: Editorial, Research

28 pages, 9470 KiB  
Review
Advancement in the Modeling and Design of Composite Pressure Vessels for Hydrogen Storage: A Comprehensive Review
by Lyazid Bouhala, Argyrios Karatrantos, Heiner Reinhardt, Norbert Schramm, Beril Akin, Alexander Rauscher, Anton Mauersberger, Senagül Tunca Taşkıran, Muhammed Erdal Ulaşlı, Engin Aktaş and Metin Tanoglu
J. Compos. Sci. 2024, 8(9), 339; https://doi.org/10.3390/jcs8090339 - 29 Aug 2024
Cited by 3 | Viewed by 3556
Abstract
The industrial and technological sectors are pushing the boundaries to develop a new class of high-pressure vessels for hydrogen storage that aim to improve durability and and endure harsh operating conditions. This review serves as a strategic foundation for the integration of hydrogen [...] Read more.
The industrial and technological sectors are pushing the boundaries to develop a new class of high-pressure vessels for hydrogen storage that aim to improve durability and and endure harsh operating conditions. This review serves as a strategic foundation for the integration of hydrogen tanks into transport applications while also proposing innovative approaches to designing high-performance composite tanks. The goal is to offer optimized, safe, and cost-effective solutions for the next generation of high-pressure vessels, contributing significantly to energy security through technological advancements. Additionally, the review deepens our understanding of the relationship between microscopic failure mechanisms and the initial failure of reinforced composites. The investigation will focus on the behavior and damaging processes of composite overwrapped pressure vessels (COPVs). Moreover, the review summarizes relevant simulation models in conjunction with experimental work to predict the burst pressure and to continuously monitor the degree of structural weakening and fatigue lifetime of COPVs. Simultaneously, understanding the adverse effects of in-service applications is vital for maintaining structural health during the operational life cycle. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Storage modes of hydrogen, source: <a href="https://www.energy.gov/eere/fuelcells/hydrogen-storage" target="_blank">https://www.energy.gov/eere/fuelcells/hydrogen-storage</a> accessed on 15 June 2024.</p>
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<p>Axial strain contour with the corresponding stacking configuration; the simulation was obtained using Abaqus software [<a href="#B27-jcs-08-00339" class="html-bibr">27</a>].</p>
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<p>Damage to composite structures. Reprinted with permission from Reference [<a href="#B32-jcs-08-00339" class="html-bibr">32</a>].</p>
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<p>Flowchart representing the MD curing procedure preceded by the initial equilibration of the liquid mixture. Curing periods were followed by annealing and equilibration phases until the target curing extent of 95% was reached. At each time step within a curing period, fix bonds and react, identify relevant reaction sites, modify their topology as necessary, and finally apply relaxation. Reprinted with permission from Reference [<a href="#B54-jcs-08-00339" class="html-bibr">54</a>].</p>
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<p>A polymer network emerged in the system during curing. (<b>a</b>) A snapshot from MD simulations of the curing reaction of a DGEBA-DDS epoxy resin of a system with 2000 and 1000 DGEBA and DDS molecules. The box length of the cubic periodic system is indicated by arrows and is approximately 11.9 nm. The largest cross-linked molecular group is shown as balls and sticks, at the point of percolation. Other groups, which are not part of the largest molecular group, are made transparent. (<b>b</b>) The molecular structures of the precursor DGEBA and the hardener DDS. The block chemistry approach does not require the usage of unchemical preactivated species, and therefore, these structures also represent the actual simulated species. Reprinted with permission from Reference [<a href="#B54-jcs-08-00339" class="html-bibr">54</a>].</p>
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<p>Multiscale modeling scheme. Reprinted with permission from Reference [<a href="#B56-jcs-08-00339" class="html-bibr">56</a>].</p>
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<p>(<b>a</b>) Variation of elastic properties along various directions in the x-y plane. (<b>b</b>) Elastic Modulus and Shear modulus for epoxy model. Reprinted with permission from [<a href="#B57-jcs-08-00339" class="html-bibr">57</a>].</p>
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<p>(<b>a</b>) Schematic diagram of an atomistic model of epoxy resin for NEMD simulation. The heat sink is located at the center of the system and the heat sources are at both ends to generate constant heat flux. (<b>b</b>) Thermal conductivities of DGEBA/4,4′-DDS as a function of degree of crosslinking from MD simulations. (<b>c</b>) Mass densities and Young’s moduli of DGEBA/4,4′-DDS as a function of degree of crosslinking from MD simulations. Reprinted with permission from [<a href="#B65-jcs-08-00339" class="html-bibr">65</a>].</p>
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<p>MD calculations of thermal expansion is superposed with experimentally measured dilatometric curves reported in Reference [<a href="#B76-jcs-08-00339" class="html-bibr">76</a>]. Reprinted with permission from [<a href="#B57-jcs-08-00339" class="html-bibr">57</a>].</p>
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<p>Diffusion coefficients of <math display="inline"><semantics> <msub> <mi>H</mi> <mn>2</mn> </msub> </semantics></math> in <math display="inline"><semantics> <mrow> <mi>P</mi> <msub> <mi>A</mi> <mn>6</mn> </msub> </mrow> </semantics></math> with 30.00% crystallinity at 288 K and different pressures. Reprinted with permission from [<a href="#B81-jcs-08-00339" class="html-bibr">81</a>].</p>
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<p>Permeability coefficients of <math display="inline"><semantics> <msub> <mi>H</mi> <mn>2</mn> </msub> </semantics></math> in PA6 with 30.00% crystallinity at 0.1 MPa and different temperatures. Reprinted with permission from [<a href="#B81-jcs-08-00339" class="html-bibr">81</a>].</p>
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<p>Dome thickness and shape influence on the strain contour of the transient region between the cylindrical part and the dome region of the tank. Reprinted with permission from [<a href="#B26-jcs-08-00339" class="html-bibr">26</a>].</p>
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<p>Postmortem picture of a hydrogen tank after burst failure. Reprinted with permission from [<a href="#B94-jcs-08-00339" class="html-bibr">94</a>].</p>
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<p>Damaged vessel obtained using Hashin criterion and the tank response using conventional shell elements model at failure for a stacking of 24 plies: (<b>a</b>) magnitude of the displacement, (<b>b</b>) yield response in the polymeric liner, (<b>c</b>) axial strain in the liner, (<b>d</b>) compression damage of the matrix in the first ply, (<b>e</b>) tensile damage of the matrix in the first ply, (<b>f</b>) damage of the matrix in tension at the third ply, (<b>g</b>) damage of the fiber in tension at the first ply, (<b>h</b>) damage of the fiber in compression at the first ply [<a href="#B37-jcs-08-00339" class="html-bibr">37</a>].</p>
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<p>Temperature and velocity distribution at fill time t = 2 s in the 2D and the 3D model. For the 3D model, plots were taken on the middle x z plane. (<b>a</b>) Temperature distribution in the 2D model, (<b>b</b>) temperature distribution in the 3D model, (<b>c</b>) velocity distribution in the 2D model, (<b>d</b>) velocity distribution in the 3D model. Reprinted with permission from Reference [<a href="#B112-jcs-08-00339" class="html-bibr">112</a>].</p>
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<p>Ultrasonic scanning detection results of the filament-wound COPV after impact: (<b>a</b>–<b>c</b>) point 1, (<b>d</b>–<b>f</b>) point 2, and (<b>g</b>–<b>i</b>) point 3. Reprinted with permission from Reference [<a href="#B116-jcs-08-00339" class="html-bibr">116</a>].</p>
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<p>Framework of the proposed method for real–time structural health monitoring using strain gauge sensors. Reprinted with permission from Reference [<a href="#B123-jcs-08-00339" class="html-bibr">123</a>].</p>
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<p>Two shapes of COPVs: (<b>a</b>) cylindrical COPV, (<b>b</b>) spherical COPV obtained by filament winding. Reprinted with permission from Reference [<a href="#B134-jcs-08-00339" class="html-bibr">134</a>].</p>
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<p>Ring-winding unit of LSE GmbH, designed and manufactured by Cetex Institute GmbH.</p>
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<p>Stress in fiber direction (S11) envelope of TCPV.</p>
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32 pages, 6776 KiB  
Review
A Review on the Modelling of Aligned Discontinuous Fibre Composites
by Chantal Lewis, Burak Ogun Yavuz, Marco L. Longana, Jonathan P.-H. Belnoue, Karthik Ram Ramakrishnan, Carwyn Ward and Ian Hamerton
J. Compos. Sci. 2024, 8(8), 318; https://doi.org/10.3390/jcs8080318 - 12 Aug 2024
Cited by 1 | Viewed by 2188
Abstract
Aligned discontinuous fibre-reinforced composites are becoming more popular because they have the potential to offer stiffness and strength comparable to their continuous counterparts along with better manufacturability. However, the modelling of highly aligned discontinuous fibre composites is still in its infancy. This paper [...] Read more.
Aligned discontinuous fibre-reinforced composites are becoming more popular because they have the potential to offer stiffness and strength comparable to their continuous counterparts along with better manufacturability. However, the modelling of highly aligned discontinuous fibre composites is still in its infancy. This paper aims to provide a comprehensive review of the available literature to understand how modelling techniques have developed and consider whether all aspects which could affect the performance of aligned discontinuous fibre composites have been addressed. Here, for the first time, a broad view of the advantages, perspectives, and limitations of current approaches to modelling the performance and behaviour of aligned discontinuous fibre composites during alignment, forming, and mechanical loading is provided in one place as a route to design optimisation. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Performance and processability of different fibre architectures. Reproduced with permission from the Journal of Multifunctional Composites, 2(3). Lancaster, PA: DEStech Publications, Inc. [<a href="#B9-jcs-08-00318" class="html-bibr">9</a>].</p>
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<p>Structure of review.</p>
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<p>Parameters affecting performance of discontinuous fibre composites.</p>
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<p>Unit cell of the composite with stairwise staggering (<b>a</b>,<b>b</b>) and random staggering (<b>c</b>,<b>d</b>). Reproduced with permission from [<a href="#B67-jcs-08-00318" class="html-bibr">67</a>].</p>
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<p>Overview of brick-and-mortar architecture. Reproduced with permission from [<a href="#B69-jcs-08-00318" class="html-bibr">69</a>].</p>
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<p>Timeline of analytical modelling theories for discontinuous fibre composites, 1952–2020.</p>
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<p>Experimental results of intermingled hybrid composites vs. predicted vales from ROM equations. Reproduced with permission from [<a href="#B24-jcs-08-00318" class="html-bibr">24</a>], CC-BY.</p>
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<p>Representative images of (<b>a</b>) RVE and (<b>b</b>) meshed RVE, with meshes on negative x, y, and positive z face for a case of in-plane aligned fibres with <math display="inline"><semantics> <msub> <mi>V</mi> <mi>f</mi> </msub> </semantics></math> of 22.4%. Reproduced with permission from [<a href="#B96-jcs-08-00318" class="html-bibr">96</a>].</p>
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<p>Representative images of (<b>a</b>) BM model of aligned fibres dispersed in a cylinder [<a href="#B119-jcs-08-00318" class="html-bibr">119</a>] and (<b>b</b>) PD model of randomly oriented fibres [<a href="#B123-jcs-08-00318" class="html-bibr">123</a>]. Reproduced with permission.</p>
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<p>Stress vs. strain curves for ADFRC with (<b>a</b>) ductile matrix and (<b>b</b>) brittle matrix. Fibre lengths from 0.2 to 2 mm are taken into consideration. Redrawn from [<a href="#B129-jcs-08-00318" class="html-bibr">129</a>].</p>
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<p>Stress vs. strain curves for ADFRC model, compared with continuous fibre results. Reproduced with permission from [<a href="#B133-jcs-08-00318" class="html-bibr">133</a>].</p>
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<p>Effect of the HiPerDiF machine plate spacing on fibre alignment. Reproduced with permission from [<a href="#B53-jcs-08-00318" class="html-bibr">53</a>].</p>
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<p>Percentage of fibres aligned within ±3° for different nozzle angles. Trend line in red. Redrawn from [<a href="#B141-jcs-08-00318" class="html-bibr">141</a>].</p>
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<p>Fibre orientation in convergent and divergent flow. Reproduced with permission from [<a href="#B145-jcs-08-00318" class="html-bibr">145</a>], CC-BY.</p>
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<p>Temperature change during thermoplastic prepreg thermoforming. Reproduced with permission from [<a href="#B161-jcs-08-00318" class="html-bibr">161</a>].</p>
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<p>Schematic showing the mechanism of tensile load transfer mechanism between aligned short fibres. Redrawn from [<a href="#B163-jcs-08-00318" class="html-bibr">163</a>], CC-BY.</p>
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<p>Plots of stress vs. strain for tensile tests at 80 °C showing real (□), calculated (x), and simulation results (—). Redrawn from [<a href="#B163-jcs-08-00318" class="html-bibr">163</a>], CC-BY.</p>
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26 pages, 2124 KiB  
Review
Material Characterization Required for Designing Satellites from Fiber-Reinforced Polymers
by Esha and Joachim Hausmann
J. Compos. Sci. 2023, 7(12), 515; https://doi.org/10.3390/jcs7120515 - 11 Dec 2023
Cited by 1 | Viewed by 3059
Abstract
This review paper discusses the effect of polymers, especially thermoplastics, in environments with low earth orbits. Space weather in terms of low earth orbits has been characterized into seven main elements, namely microgravity, residual atmosphere, high vacuum, atomic oxygen, ultraviolet and ionization radiation, [...] Read more.
This review paper discusses the effect of polymers, especially thermoplastics, in environments with low earth orbits. Space weather in terms of low earth orbits has been characterized into seven main elements, namely microgravity, residual atmosphere, high vacuum, atomic oxygen, ultraviolet and ionization radiation, solar radiation, and space debris. Each element is discussed extensively. Its effect on polymers and composite materials has also been studied. Quantification of these effects can be evaluated by understanding the mechanisms of material degradation caused by each environmental factor along with its synergetic effect. Hence, the design elements to mitigate the material degradation can be identified. Finally, a cause-and-effect diagram (Ishikawa diagram) is designed to characterize the important design elements required to investigate while choosing a material for a satellite’s structure. This will help the designers to develop experimental methodologies to test the composite material for its suitability against the space environment. Some available testing facilities will be discussed. Some potential polymers will also be suggested for further evaluation. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Source of heat for a satellite.</p>
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<p>Spectral irradiance at low earth orbit.</p>
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<p>Cause and effect diagram of design requirement and its characteristics.</p>
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21 pages, 1640 KiB  
Review
Review on Characterization of Biochar Derived from Biomass Pyrolysis via Reactive Molecular Dynamics Simulations
by Zhong Hu and Lin Wei
J. Compos. Sci. 2023, 7(9), 354; https://doi.org/10.3390/jcs7090354 - 25 Aug 2023
Cited by 10 | Viewed by 4516
Abstract
Biochar is a carbon-rich solid produced during the thermochemical processes of various biomass feedstocks. As a low-cost and environmentally friendly material, biochar has multiple significant advantages and potentials, and it can replace more expensive synthetic carbon materials for many applications in nanocomposites, energy [...] Read more.
Biochar is a carbon-rich solid produced during the thermochemical processes of various biomass feedstocks. As a low-cost and environmentally friendly material, biochar has multiple significant advantages and potentials, and it can replace more expensive synthetic carbon materials for many applications in nanocomposites, energy storage, sensors, and biosensors. Due to biomass feedstock species, reactor types, operating conditions, and the interaction between different factors, the compositions, structure and function, and physicochemical properties of the biochar may vary greatly, traditional trial-and-error experimental approaches are time consuming, expensive, and sometimes impossible. Computer simulations, such as molecular dynamics (MD) simulations, are an alternative and powerful method for characterizing materials. Biomass pyrolysis is one of the most common processes to produce biochar. Since pyrolysis of decomposing biomass into biochar is based on the bond-order chemical reactions (the breakage and formation of bonds during carbonization reactions), an advanced reactive force field (ReaxFF)-based MD method is especially effective in simulating and/or analyzing the biomass pyrolysis process. This paper reviewed the fundamentals of the ReaxFF method and previous research on the characterization of biochar physicochemical properties and the biomass pyrolysis process via MD simulations based on ReaxFF. ReaxFF implicitly describes chemical bonds without requiring quantum mechanics calculations to disclose the complex reaction mechanisms at the nano/micro scale, thereby gaining insight into the carbonization reactions during the biomass pyrolysis process. The biomass pyrolysis and its carbonization reactions, including the reactivity of the major components of biomass, such as cellulose, lignin, and hemicellulose, were discussed. Potential applications of ReaxFF MD were also briefly discussed. MD simulations based on ReaxFF can be an effective method to understand the mechanisms of chemical reactions and to predict and/or improve the structure, functionality, and physicochemical properties of the products. Full article
(This article belongs to the Special Issue Characterization and Modelling of Composites, Volume III)
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<p>Some bond orders considered in ReaxFF potential forms.</p>
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<p>Schematic representations of uncorrected and corrected bond order in terms of interatomic distance vs. carbon–carbon bond order to be considered.</p>
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<p>Schematic structure of cellulose (C<sub>6</sub>H<sub>10</sub>O<sub>5</sub>)<sub>n</sub>.</p>
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<p>Schematic basic units of lignin polymer: (<b>a</b>) coniferyl, (<b>b</b>) sinapyl, and (<b>c</b>) p-coumaryl alcohol structures.</p>
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<p>Schematic structure of lignin, where the purple wavy lines represent the continuing of the molecule.</p>
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<p>Schematic structure of xylan, where the purple wavy lines represent the continuing of the molecule.</p>
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