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Materials, Volume 17, Issue 12 (June-2 2024) – 257 articles

Cover Story (view full-size image): A new UV-curable composite material with a poly(ethylene glycol diacrylate) matrix with unmodified and methacryloxyl-grafted TiO2 and TiO2-ZrO2 systems is a promising candidate for the next generation of medical component coatings. The applied filler functionalization process resulted in a decrease in its polarity and a change in its size, BET surface area, and pore volume, which influenced the viscosity and kinetics of the photocurable system. Modification of TiO2 with ZrO2 altered the properties of the light-cured composition. Compositions with TZ and TZM were found to have low photopolymerization initiation ability. The thermal stability of composite materials improves with increasing filler content, making them suitable for many packaging applications. The hydrophobicity of the TiO2-based compound improved with UV irradiation, providing possible applications in stomatology. View this paper
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28 pages, 8727 KiB  
Article
Microstructural and Electrochemical Study: Pitting Corrosion Mechanism on A390 Al–Si Alloy and Ce–Mo Treatment as a Better Corrosion Protection
by Héctor Herrera Hernández, Araceli Mandujano Ruiz, Carlos Omar González Morán, José Guadalupe Miranda Hernández, José de Jesús Agustín Flores Cuautle, Jorge Morales Hernández and Irma Hernández Casco
Materials 2024, 17(12), 3044; https://doi.org/10.3390/ma17123044 - 20 Jun 2024
Viewed by 1141
Abstract
Sulfuric acid anodizing assisted by a hydrothermal sealing with inhibitors [Ce3+-Mo6+] was used to prevent pitting corrosion on spray-deposited hypereutectic Al–Si alloy (A390). An investigation concerning the evaluation of pitting corrosion resistance on the anodic oxide thin film with [...] Read more.
Sulfuric acid anodizing assisted by a hydrothermal sealing with inhibitors [Ce3+-Mo6+] was used to prevent pitting corrosion on spray-deposited hypereutectic Al–Si alloy (A390). An investigation concerning the evaluation of pitting corrosion resistance on the anodic oxide thin film with ions incorporated was carried out in NaCl solution using electrochemical measurements (i.e., potentiodynamic polarization and electrochemical impedance spectroscopy, EIS). The influence of Si phase morphology and size on the growth mechanism of an anodic oxide film was characterized by scanning electron microscopy (SEM) and X-ray diffraction (XRD). The results were then compared with those for its equivalent IM390 alloy (Al-17Si-4.5Cu-0.6Mg) produced through a conventional process ingot metallurgy, IM. The electrochemical findings indicate that sulfuric acid anodizing followed by a simple hot water sealing treatment was ineffective. In this manner, an intense attack was localized by pitting corrosion that occurred on the anodic oxide film in less than three days, as denoted by characteristic changes in the EIS spectra at the lowest frequencies. Improved results were achieved for Ce–Mo surface modification, which can provide better corrosion resistance on the aluminum alloys because no signs of pits were observed during the corrosion testing. Full article
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<p>Schematic illustration of the experimental process used to produce Al–Si alloys through spray-atomization and deposition technology at the University of California, Irvine UCI [<a href="#B75-materials-17-03044" class="html-bibr">75</a>,<a href="#B76-materials-17-03044" class="html-bibr">76</a>].</p>
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<p>Transversal section of spray deposits of hypereutectic Al–Si alloy produced under different thermal conditions.</p>
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<p>Optical micrographs of the cross-section of Al–Si powder produced by nitrogen gas atomization show a spherical shape of the powder particles (<b>a</b>) and fine silicon precipitation in the aluminum matrix (<b>b</b>).</p>
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<p>Cross-sectional view of a cold-spray-deposited (CSD) Al–Si alloy showing the microstructure of three regions: Region “A” is adjacent to the substrate surface. Region “B” is the central portion. Region “C” is near the upper surface.</p>
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<p>Micrographs of Al–Si preforms showing (<b>a</b>) grains morphology and Si particles of as-sprayed deposit HSD, (<b>b</b>) fine uniform precipitation as-sprayed deposit CSD, and (<b>c</b>) Si and eutectic phase in IM390 ingot alloy.</p>
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<p>Micrographs of Al–Si extrudates showing grain morphology and Si particles; (<b>a</b>) coarser dispersion in extrudate as-sprayed deposit HSD, (<b>b</b>) fine uniform precipitation of extrudate from as-sprayed deposit CSD, and (<b>c</b>) Si and eutectic phase in IM390 casting alloy.</p>
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<p>X-ray diffraction patterns of Al–Si alloy as-sprayed deposits and their corresponding extrudates products; also included is the IM390 casting alloy as reference. Insets; a* Al<sub>2</sub>Cu precipitates on (110) plane at 20.7°, b* Al<sub>2</sub>Cu precipitation on (112) plane at 38.3°, c* precipitates on (420) plane at 69.7°.</p>
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<p>Potentiodynamic polarization curves of Al–Si alloys in 3.5% NaCl. As-received condition for the spray-deposited CSD or HSD and its extrusion product; IM390 casting alloy response is also shown as comparative behavior. (<b>a</b>) HSD hot spray deposit (2.5 m<sup>3</sup>/kg), (<b>b</b>) CSD cold spray deposit (4 m<sup>3</sup>/kg), (<b>c</b>) Extruded bar at 480° C for CSD, (<b>d</b>) IM390 ingot casting process.</p>
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<p>Schematic illustration of the Al/Si galvanic coupling that causes the mechanism of pitting corrosion in Al–Si alloys in 3.5% NaCl.</p>
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<p>Surface appearance showing galvanic corrosion mechanism on as-casted Al–Si alloy (IM390) after exposure to 3.5% NaCl, as received condition.</p>
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<p>EIS spectra in Nyquist form of as-received Al–Si alloys immersed in 3.5% NaCl with respect to the exposure time. (<b>a</b>) Cold-spray deposit CSD and (<b>b</b>) IM390 alloy. Insets show a detailed view of pit initiation frequencies as Bode plots.</p>
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<p>Representation of the simulation response of the equivalent electrical circuits (EECs) used to model the impedance behavior of Al–Si materials exposed for 7 days in 3.5% NaCl.</p>
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<p>Total capacitance Ct of as-received Al–Si alloys (as-sprayed deposit and IM390-ingot molding) exposed for 7 days in 3.5% NaCl.</p>
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<p>Plot of log (1/R<sup>o</sup><sub>pit</sub>) vs. log <span class="html-italic">t</span> of as-received Al–Si alloys (as-sprayed deposit and IM390-ingot molding) exposed for 7 days in 3.5% NaCl.</p>
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<p>Potential transients of as-received spray deposit CSD exposed for 7 days in 3.5% NaCl. Note: The insets show the amplitude of the transient magnitude for pitting corrosion. Transient 1 for 2 h of immersion, 2 for 1 day, 3 is not shown for clearness of the plot and 4 for 7 days.</p>
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<p>Anodic polarization curves for the H<sub>2</sub>SO<sub>4</sub> anodized cold-spray-deposited Al–Si alloy that was hydrothermally sealed in different reagents: HWS; CeSM; and Ce–MoSM. Inset a SEM micrographs show anodic film morphology after hydrothermal sealing.</p>
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<p>Impedance results for H<sub>2</sub>SO<sub>4</sub> anodized spray-deposited Al–Si alloy and passivated in (<b>a</b>) hot water for 60 min, (<b>b</b>) 10 mM CeCl<sub>3</sub> for 20 min, and (<b>c</b>) 10 mM CeCl<sub>3</sub> and 10 mM Na<sub>2</sub>MoO<sub>4</sub> for 20 min, tested in 3.5% NaCl as a function of exposure time.</p>
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<p>Representation of the simulation response of the equivalent electrical circuits (EECs) used to model the impedance behavior of H<sub>2</sub>SO<sub>4</sub> anodized cold-spray-deposited Al–Si alloy exposed for 7 days in 3.5% NaCl.</p>
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<p>SEM images showing the surface appearance of Al–Si alloy after exposure to 3.5% NaCl for 7 days. (<b>a</b>) pit propagation on Al matrix, (<b>b</b>) spherical pit distribution on the Al matrix.</p>
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<p>SEM images of Al–Si alloy showing the surface appearance of cerium surface modification process (CeSM) after exposure to 3.5% NaCl for 7 days. (<b>a</b>) hot water sealing HWS, (<b>b</b>) cerium sealing CeSM, (<b>c</b>) EDS shows Ce ions on the anodic film, (<b>d</b>) CeSM treatment applied on the IM390 alloy.</p>
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15 pages, 3864 KiB  
Article
Effect of Single Particle High-Speed Impingement on the Electrochemical Step Characteristics of a Stainless-Steel Surface
by Meihong Liu, Long Chai, Min Yang and Jiarui Cheng
Materials 2024, 17(12), 3043; https://doi.org/10.3390/ma17123043 - 20 Jun 2024
Viewed by 694
Abstract
In the process of particle erosion and electrochemical corrosion interaction, the electrolyte flow state change, product film destruction, and matrix structure change caused by particle impact affect the electrochemical corrosion process. Such transient, complex physical and electrochemical changes are difficult to capture because [...] Read more.
In the process of particle erosion and electrochemical corrosion interaction, the electrolyte flow state change, product film destruction, and matrix structure change caused by particle impact affect the electrochemical corrosion process. Such transient, complex physical and electrochemical changes are difficult to capture because of the short duration of action and the small collision area. The peak, step time, and recovery time in this transient step cycle can indirectly reflect the smoothness and reaction rate of the electrochemical reaction system, and thus characterize the resistance to scouring corrosion coupling damage of metals in liquid–solid two-phase flow. In this study, in order to obtain the electrochemical response at the moment of particle impact, electrochemical monitoring experiments using a specially designed miniature three-electrode system were used to test step-critical values, including step potential, current, and resistance, among others. Meanwhile, an electrochemical step model under particle impact considering boundary layer perturbation was developed. The experimental results reflect the effect law of particle impact velocity and particle size on the peak step and recovery period. Meanwhile, the effect of particle impingement on the electrochemical step of stainless steel in different electrolyte solutions was obtained by comparing the step curves in distilled water and Cl-containing water. The connection between the parameters in the electrochemical step model and in the particle impact, as well as the effect of the variation of these parameters on the surface repassivation process are discussed in this paper. By fitting and modeling the test curves, a new mathematical model of electrochemical step-decay under single-particle impact was obtained, which can be used to characterize the change pattern of electrochemical parameters on the metal surface before and after the impingement. Full article
(This article belongs to the Special Issue Corrosion and Mechanical Behavior of Metal Materials (2nd Edition))
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<p>Diagram of particle impact experiment.</p>
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<p>Diagram of three-electrode setup for particle impact electrochemical experiment.</p>
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<p>Single-particle impact experiment using plastic particles.</p>
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<p>Experimental results of potential variation of 304 stainless steel under single particle impact in distilled water (flow rate comparison). (<b>a</b>) 4 mm, (<b>b</b>) 6 mm, (<b>c</b>) 8 mm, (<b>d</b>) 10 mm, (<b>e</b>) 12 mm.</p>
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<p>Experimental results of potential variation of 304 stainless steel under single particle impact in distilled water (comparison by particle diameter). (<b>a</b>) 1 m/s, (<b>b</b>) 2 m/s, (<b>c</b>) 3 m/s, (<b>d</b>) 4 m/s, (<b>e</b>) 5 m/s.</p>
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<p>Experimental results of surface current density variation of 304 stainless steel subjected to single particle impact in water (comparison of flow velocities). (<b>a</b>) 4 mm, (<b>b</b>) 6 mm, (<b>c</b>) 8 mm, (<b>d</b>) 10 mm, (<b>e</b>) 12 mm.</p>
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<p>Experimental results of surface current density variation of 304 stainless steel subjected to single particle impact in water (comparison of particle diameters). (<b>a</b>) 1 m/s, (<b>b</b>) 2 m/s, (<b>c</b>) 3 m/s, (<b>d</b>) 4 m/s, (<b>e</b>) 5 m/s.</p>
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<p>Experimental results of surface current density variation of 304 stainless steel under single particle impact in 3.5 wt% NaCl solution (comparison of flow rates). (<b>a</b>) 4 mm, (<b>b</b>) 6 mm, (<b>c</b>) 8 mm, (<b>d</b>) 10 mm, (<b>e</b>) 12 mm.</p>
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<p>Experimental results of surface current density variation of 304 stainless steel under single particle impact in 3.5 wt% NaCl solution (comparison of particle diameters). (<b>a</b>) 1 m/s, (<b>b</b>) 2 m/s, (<b>c</b>) 3 m/s, (<b>d</b>) 4 m/s, (<b>e</b>) 5 m/s.</p>
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<p>The schematic diagram illustrates the trend of current density variation caused by particle impact on the metal surface.</p>
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21 pages, 9899 KiB  
Article
Alternative Method for Determination of Vibroacoustic Material Parameters for Building Applications
by Krzysztof Nering and Konrad Nering
Materials 2024, 17(12), 3042; https://doi.org/10.3390/ma17123042 - 20 Jun 2024
Cited by 1 | Viewed by 931
Abstract
The development of urbanization and the resulting expansion of residential and transport infrastructures pose new challenges related to ensuring comfort for city dwellers. The emission of transport vibrations and household noise reduces the quality of life in the city. To counteract this unfavorable [...] Read more.
The development of urbanization and the resulting expansion of residential and transport infrastructures pose new challenges related to ensuring comfort for city dwellers. The emission of transport vibrations and household noise reduces the quality of life in the city. To counteract this unfavorable phenomenon, vibration isolation is widely used to reduce the propagation of vibrations and noise. A proper selection of vibration isolation is necessary to ensure comfort. This selection can be made based on a deep understanding of the material parameters of the vibration isolation used. This mainly includes dynamic stiffness and damping. This article presents a comparison of the method for testing dynamic stiffness and damping using a single degree of freedom (SDOF) system and the method using image processing, which involves tracking the movement of a free-falling steel ball onto a sample of the tested material. Rubber granules, rubber granules with rubber fibers, and rebound polyurethanes were selected for testing. Strong correlations were found between the relative indentation and dynamic stiffness (at 10–60 MN/m3) and the relative rebound and damping (for 6–12%). Additionally, a very strong relationship was determined between the density and fraction of the critical damping factor/dynamic stiffness. The relative indentation and relative rebound measurement methods can be used as an alternative method to measure the dynamic stiffness and critical damping factor, respectively. Full article
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<p>Samples used for research in this article. Tested materials are rubber granulate (S), rubber granulate with rubber fibers (F), and rebound polyurethane (P).</p>
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<p>Physical model of the mass–damper–spring system with single degree of freedom (SDOF).</p>
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<p>Schematic presentation of the half-power bandwidth method using the displacement spectrum. <span class="html-italic">X<sub>r</sub></span>—displacement amplitude, <span class="html-italic">f<sub>r</sub></span>—resonant frequency, and <span class="html-italic">f</span><sub>1</sub> and <span class="html-italic">f</span><sub>2</sub>—correspond to frequencies to 0.7 value of resonance amplitude.</p>
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<p>Dynamic stiffness test bench with loaded sample. One square in photograph is one centimeter.</p>
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<p>Pseudo-displacement response spectrum of sample P150 (288 kg/m<sup>3</sup>) with resonant frequency of 35.2 Hz and critical damping factor 0.0645.</p>
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<p>Test bench for ball-tracking experiment.</p>
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<p>Test bench diagram.</p>
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<p>Examples of ball-tracking results for the P150 sample with a density of 288 kg/m<sup>3</sup>. (<b>a</b>) shows full motion of the ball, and (<b>b</b>) shows magnification in ball drop area.</p>
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<p>Comparison of different models of dynamic stiffness and relative indentation relationship. (<b>a</b>) model Power1 val(x) = a·x<sup>b</sup>, where a = 7.834, b = −0.4115, and R<sup>2</sup> = 0.5435 and (<b>b</b>) model Linear val(x) = p1·x + p2, where p1 = −899.6, p2 = 61.65, and R<sup>2</sup> = 0.8587.</p>
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<p>Comparison of different models of dynamic stiffness and relative indentation relationship with exclusion of S1000 (relative indentation &lt; 0.01). (<b>a</b>) model Power1 val(x) = a·x<sup>b</sup>, where a = 2.000, b = −0.777, and R<sup>2</sup> = 0.8381 and (<b>b</b>) model Linear val(x) = p1·x + p2, where p1 = −1036, p2 = 66.95, and R<sup>2</sup> = 0.9468.</p>
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<p>Comparison of different models of critical damping factor and first relative rebound relationship. (<b>a</b>) model Logarithmic val(x) = a·log10(x), where a = −0.2492 and R<sup>2</sup> = 0.7654 and (<b>b</b>) model Linear val(x) = p1·x + p2, where p1 = −0.3325, p2 = 0.2368, and R<sup>2</sup> = 0.8149.</p>
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<p>Comparison of different models of critical damping factor and first and second relative rebound (averaged) relationship. (<b>a</b>) model Logarithmic val(x) = a·log10(x), where a = −0.2568 and R<sup>2</sup> = 0.7809 and (<b>b</b>) model Linear val(x) = p1·x + p2, where p1 = −0.3143, p2 = 0.2321, and R<sup>2</sup> = 0.8123.</p>
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<p>Models of Power2 (val(x) = a·x<sup>b</sup> + c) describing relationship between (<b>a</b>) dynamic stiffness and density where a = −1.422 × 10<sup>6</sup>, b = −2.105, c = 49.53, and R<sup>2</sup> = 0.8842 and (<b>b</b>) critical damping factor and density where a = 2.201 × 10<sup>−15</sup>, b = 4.433, c = 0.07053, and R<sup>2</sup> = 0.6301.</p>
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<p>The fraction Critical damping factor/Dynamic stiffness as a function of density described with the usage of Exp2 model (val(x) = a·exp(b·x) + c·exp(d·x)), a = 0.04442, b = −0.01349, c = 0.0005713, d = 0.001433, and R<sup>2</sup> = 0.9460.</p>
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<p>Rayleigh damping model (val(x) = 1/2·(a·x + b/x)), where a = 0.001935, b = 2.273, and R<sup>2</sup> = 0.2385.</p>
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<p>Rayleigh-ish damping model based on dynamic stiffness instead of resonant frequency (val(x) = 1/2·(a·x + b/x)), where a = 0.003327, b = 1.029, and R<sup>2</sup> = 0.3730.</p>
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15 pages, 3261 KiB  
Article
Recovery of Plastics from WEEE through Green Sink–Float Treatment
by Annarita Fiorente, Germano D’Agostino, Andrea Petrella, Francesco Todaro and Michele Notarnicola
Materials 2024, 17(12), 3041; https://doi.org/10.3390/ma17123041 - 20 Jun 2024
Cited by 1 | Viewed by 973
Abstract
Increasing demand for electrical and electronic equipment results in the generation of a rapidly growing waste stream, known by the acronym WEEE (waste electrical and electronic equipment). The purpose of this study was to evaluate the effectiveness of green sink–float treatment in sorting [...] Read more.
Increasing demand for electrical and electronic equipment results in the generation of a rapidly growing waste stream, known by the acronym WEEE (waste electrical and electronic equipment). The purpose of this study was to evaluate the effectiveness of green sink–float treatment in sorting plastic polymers typically found in WEEE (PP, ABS, PA6, PS, and PVC). Molasses, a by-product of sugar bio-refining, was added in various concentrations to water to form solutions at different densities. The methodology was initially tested on virgin polymers; later, it was applied to plastics from a WEEE treatment plant. The polymers were characterised through near infrared spectroscopy (NIRS) and Fourier-transform infrared spectroscopy (FTIRS) analyses; the detection of any additives and flame retardants was conducted using the sliding spark technology (SSS2) and scanning electron microscope (SEM—EDX). The results showed that, for plastics from WEEE, the recovery efficiency was 55.85% for PP in a solution of tap water while the remaining part of PP (44.15%) was recovered in a solution of water to which 90% molasses was added. Furthermore, 100% recovery efficiency was obtained for PS and 93.73% for ABS in a solution of tap water with the addition of 10% w/v molasses. A recovery efficiency of 100% was obtained for PVC and 100% for PA6 in a solution consisting solely of molasses. Full article
(This article belongs to the Section Advanced Composites)
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<p>Sink–float methodology applied to virgin polymers.</p>
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<p>Sink–float methodology applied to polymers from WEEE treatment plant.</p>
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<p>(<b>a</b>) Composition of the sample of virgin plastics; (<b>b</b>) Composition of plastics from WEEE.</p>
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<p>FTIR spectra of representative samples of plastic polymers in R2 WEEE: (1) PP, (2) ABS, (3) PVC, (4) PS e, (5) PA6. The black line refers to virgin polymers and the red line to polymers from WEEE.</p>
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<p>SEM images of ABS and PP plastic samples from WEEE with distribution maps.</p>
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<p>Flow chart of virgin polymers recovery by the sink–float method.</p>
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<p>Flow chart of the plastics from WEEE recovery by the sink–float method.</p>
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<p>Results obtained from the sink–float process applied to virgin polymers and polymers from WEEE in terms of recovery efficiency.</p>
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18 pages, 5241 KiB  
Article
Thermo-Chemo-Mechanical Modeling of Residual Stress in Unidirectional Carbon Fiber-Reinforced Polymers during Manufacture
by Rui Bao, Junpeng Liu, Zhongmin Xiao and Sunil C. Joshi
Materials 2024, 17(12), 3040; https://doi.org/10.3390/ma17123040 - 20 Jun 2024
Cited by 1 | Viewed by 954
Abstract
The application of carbon fiber-reinforced composite materials in marine engineering is growing steadily. The mechanical properties of unbonded flexible risers using composite tensile armor wire are highly valued. However, the curing process generates a certain amount of internal residual stress. We present a [...] Read more.
The application of carbon fiber-reinforced composite materials in marine engineering is growing steadily. The mechanical properties of unbonded flexible risers using composite tensile armor wire are highly valued. However, the curing process generates a certain amount of internal residual stress. We present a detailed analysis of epoxy resin laminates to assess the impact of thermal, chemical, and mechanical effects on the curing stress and strain. An empirical model that correlates temperature and degree of cure was developed to precisely fit the elastic modulus data of the curing resin. The chemical kinetics of the epoxy resin system was characterized using differential scanning calorimetry (DSC), while the tensile relaxation modulus was determined through a dynamic mechanical analysis. The viscoelastic model was calibrated using the elastic modulus data of the cured resin combining temperature and degree of the curing (thermochemical kinetics) responses. Based on the principle of time–temperature superposition, the displacement factor and relaxation behavior of the material were also accurately captured by employing the same principle of time–temperature superposition. Utilizing the empirical model for degree of cure and modulus, we predicted micro-curing-induced strains in cured composite materials, which were then validated with experimental observations. Full article
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<p>Structure of unbounded flexible risers in deep water.</p>
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<p>Location of FBG sensors and thermocouple for strain measurement.</p>
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<p>The geometry and mesh of the finite element model.</p>
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<p>Development of the degree of cure in the central point of the laminate. During the curing process of thick laminates, the curing speed is different between the interior and the surface of the material. The temperature gradients cause inconsistent thermal expansion and contraction. This inconsistency can result in residual stress within the laminate, potentially causing warping, deformation, and even cracking of the laminate, thereby compromising its dimensional stability and structural integrity. Additionally, different degrees of cure between the inner and the outer layers can result in uneven crosslinking density, leading to disparities in the mechanical properties (such as strength and toughness) in different locations, thus reducing the overall performance and reliability of the material. Furthermore, uneven solidification during the curing process can introduce defects such as uncured areas or bubbles, increasing the risk of material failure during service. An optimized curing process is necessary to overcome these challenges, requiring real-time monitoring systems to ensure uniform curing and high-quality laminate performance.</p>
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<p>Heat flux based on the temperature at different heating rates.</p>
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<p>Fit relationship diagram for the Nth-order reaction kinetics model.</p>
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<p>Relationship between activation energy and degree of cure for the curing process.</p>
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<p>Comparison of the cure rate profiles at different heating rates.</p>
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<p>Degree of cure at different heating rates.</p>
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<p>Relaxation modulus for the epoxy system and its master curve.</p>
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<p>Shift factors for the relaxation modulus.</p>
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<p>(<b>a</b>) Elastic modulus of the cured resin at different frequencies; (<b>b</b>) loss factor at different frequencies.</p>
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<p>Development of longitudinal stress during the cure cycles in the examined laminates.</p>
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<p>Development of transverse stress during the cure cycles in the examined laminates.</p>
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<p>Longitudinal curing strain during the manufacturing process.</p>
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<p>Transverse curing strain during the manufacturing process.</p>
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18 pages, 8081 KiB  
Article
Study on Spline Stress of Separator Plates in a Wet Multi-Plate Clutch
by Biao Ma, Xiaobo Chen, Changsong Zheng, Liang Yu, Qin Zhao and Weichen Lu
Materials 2024, 17(12), 3039; https://doi.org/10.3390/ma17123039 - 20 Jun 2024
Viewed by 816
Abstract
The spline teeth fracture of separator plates in wet multi-plate clutches compromises driving safety and the vehicle’s lifespan. Tooth fracture is mainly caused by stress concentration at the tooth root and uneven circumferential load distribution. This paper considers parameters such as torque, teeth [...] Read more.
The spline teeth fracture of separator plates in wet multi-plate clutches compromises driving safety and the vehicle’s lifespan. Tooth fracture is mainly caused by stress concentration at the tooth root and uneven circumferential load distribution. This paper considers parameters such as torque, teeth count, tooth profile, and misalignment errors, establishing the corresponding finite element (FE) model to analyze the impact of the above-mentioned parameters on the strength of the separator plates. Analysis under even and biased load circumstances demonstrated that an optimum tooth count and profile can significantly increase the strength of the separator plates, offering advice for the optimized design of wet multi-plate clutch separator plates. Full article
(This article belongs to the Section Advanced Materials Characterization)
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<p>A wet multi-plate clutch and the separator plates’ tooth fracture and crack.</p>
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<p>Misalignment error model.</p>
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<p>Force diagram for the separator plate and single teeth.</p>
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<p>FE model.</p>
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<p>Stress distribution results under even load conditions.</p>
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<p>Max stress results for torque and tooth count variables.</p>
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<p>Simulation results of trapezoidal teeth with varying pressure angles: (<b>a</b>) trapezoidal profiles with different pressure angles; (<b>b</b>) max stress results for tooth profile variables.</p>
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<p>Comparison diagram of contact stress for different trapezoidal teeth.</p>
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<p>Equivalent stress distribution and deformation characteristics under angular misalignment.</p>
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<p>Stress distribution of each tooth on separator plates under different angular misalignment conditions and tooth counts: (<b>a</b>) 12 teeth; (<b>b</b>) 18 teeth; (<b>c</b>) 24 teeth.</p>
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<p>Stress distribution of each tooth on separator plates under different angular misalignment conditions and tooth profiles: (<b>a</b>) rectangular tooth; (<b>b</b>) involute tooth; (<b>c</b>) trapezoidal tooth.</p>
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<p>Variation characteristics of the unevenness coefficient and peak stress under different tooth counts: (<b>a</b>) unevenness coefficient; (<b>b</b>) peak stress.</p>
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<p>Variation characteristics of the unevenness coefficient and maximum stress under different tooth profiles and angular offset: (<b>a</b>) unevenness coefficient; (<b>b</b>) peak stress.</p>
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<p>Equivalent stress distribution and deformation characteristics under radial misalignment.</p>
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<p>Stress distribution of each tooth on separator plates under different radial misalignment conditions and tooth counts: (<b>a</b>) 12 teeth; (<b>b</b>) 18 teeth; (<b>c</b>) 24 teeth.</p>
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<p>Variation characteristics of the unevenness coefficient and maximum stress under different tooth counts: (<b>a</b>) unevenness coefficient; (<b>b</b>) peak stress.</p>
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<p>Variation characteristics of the count of the loaded teeth under radial misalignment and different tooth counts and profiles: (<b>a</b>) teeth count; (<b>b</b>) teeth profile.</p>
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<p>Stress distribution of each tooth on the separator plate under different radial misalignment conditions and tooth profiles: (<b>a</b>) rectangular tooth; (<b>b</b>) involute tooth; (<b>c</b>) trapezoidal tooth.</p>
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<p>Variation characteristics of the unevenness coefficient and maximum stress under different tooth profiles and radial offset: (<b>a</b>) unevenness coefficient; (<b>b</b>) peak stress.</p>
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13 pages, 2343 KiB  
Article
Thermodynamic Model for Hydrogen Production from Rice Straw Supercritical Water Gasification
by Zhigang Liu, Zhiyong Peng, Lei Yi, Le Wang, Jingwei Chen, Bin Chen and Liejin Guo
Materials 2024, 17(12), 3038; https://doi.org/10.3390/ma17123038 - 20 Jun 2024
Viewed by 1018
Abstract
Supercritical water gasification (SCWG) technology is highly promising for its ability to cleanly and efficiently convert biomass to hydrogen. This paper developed a model for the gasification of rice straw in supercritical water (SCW) to predict the direction and limit of the reaction [...] Read more.
Supercritical water gasification (SCWG) technology is highly promising for its ability to cleanly and efficiently convert biomass to hydrogen. This paper developed a model for the gasification of rice straw in supercritical water (SCW) to predict the direction and limit of the reaction based on the Gibbs free energy minimization principle. The equilibrium distribution of rice straw gasification products was analyzed under a wide range of parameters including temperatures of 400–1200 °C, pressures of 20–50 MPa, and rice straw concentrations of 5–40 wt%. Coke may not be produced due to the excellent properties of supercritical water under thermodynamic constraints. Higher temperatures, lower pressures, and biomass concentrations facilitated the movement of the chemical equilibrium towards hydrogen production. The hydrogen yield was 47.17 mol/kg at a temperature of 650 °C, a pressure of 25 MPa, and a rice straw concentration of 5 wt%. Meanwhile, there is an absorptive process in the rice straw SCWG process for high-calorific value hydrogen production. Energy self-sufficiency of the SCWG process can be maintained by adding small amounts of oxygen (ER < 0.2). This work would be of great value in guiding rice straw SCWG experiments. Full article
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<p>Comparison of simulation results with the experimental results under different gasification temperatures (glycerol, 24.1 MPa, 5 wt%).</p>
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<p>Effect of temperature on product distribution (25 MPa, 10 wt% rice straw).</p>
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<p>Effect of pressure on product distribution (650 °C, 10 wt% rice straw).</p>
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<p>Effect of rice straw concentration on product distribution (650 °C, 25 MPa).</p>
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<p>Reaction heat duty and HHV of gaseous products under operating parameters.</p>
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<p>Reaction heat duty and HHV of gaseous products under operating parameters.</p>
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13 pages, 7695 KiB  
Article
Texture-Differentiated Grain Growth in Silicon Steel: Experiments and Modeling
by Songtao Chang, Yuhui Sha, Gengsheng Cao, Fang Zhang and Liang Zuo
Materials 2024, 17(12), 3037; https://doi.org/10.3390/ma17123037 - 20 Jun 2024
Viewed by 776
Abstract
Grain growth for various texture components in silicon steel was investigated via experiments and modeling. It was found that the clustered spatial arrangement of grains with specific orientations significantly altered the local environment for grain growth and consequently resulted in texture-differentiated grain size [...] Read more.
Grain growth for various texture components in silicon steel was investigated via experiments and modeling. It was found that the clustered spatial arrangement of grains with specific orientations significantly altered the local environment for grain growth and consequently resulted in texture-differentiated grain size distribution (GSD) evolution. A novel local-field model was proposed to describe grain growth driven by continuous changing orientation and size distribution of adjacent grains. The modelling results show that the texture-differentiated grain growth in microstructure with grain clusters can produce a GSD with increased proportion in small-sized range and large-sized range by more than two-times, accompanied with an evident change in area fractions of various texture components. The effect of clustered spatial arrangement on grain growth can be precisely predicted, which is valuable to design and control the texture-differentiated GSD as well as the global GSD. Full article
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<p>Orientation image maps and constant <span class="html-italic">φ</span><sub>2</sub> = 0° and 45° sections of ODFs in primarily recrystallized (<b>a</b>,<b>c</b>,<b>e</b>) and annealed (<b>b</b>,<b>d</b>,<b>f</b>) silicon steel sheets.</p>
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<p>Grain boundary misorientation distributions for all grains and major texture components in primarily recrystallized (<b>a</b>) and annealed (<b>b</b>) silicon steel sheets.</p>
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<p>Orientation image maps of identical region of Goss grain clusters and surrounding matrix grains in primarily recrystallized (<b>a</b>,<b>c</b>,<b>e</b>) and annealed (<b>b</b>,<b>d</b>,<b>f</b>) silicon steel sheets. The regions of Goss grain clusters in primarily recrystallized sheets (marked as A, B, and C) and the identical region in further annealed sheets are depicted with black dashed lines. G1 and G2 are two grains with Σ5 and Σ9 boundaries between Goss grains, respectively.</p>
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<p>Area fraction, average grain size, and maximum grain size in primarily recrystallized and annealed silicon steel sheets.</p>
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<p>Grain size distribution in primarily recrystallized and annealed silicon steel sheets.</p>
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<p>Representation of local-field model: (<b>a</b>) planar section of three-dimensional microstructure in polycrystalline materials, (<b>b</b>) planar section of three-dimensional microstructure with spherical grains, and (<b>c</b>) grain network in a planar section.</p>
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<p>Measured and calculated grain size distributions for major texture components after grain growth annealing in silicon steel sheets.</p>
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<p>Schematic of initial microstructure (<b>a</b>) and grain size distribution (<b>b</b>) for the case of specially oriented grains clusteringly and randomly embedded in randomly oriented grains used in <a href="#sec4dot2-materials-17-03037" class="html-sec">Section 4.2</a>.</p>
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<p>The evolution of average grain size (<b>a</b>), area fraction (<b>b</b>), and grain size distribution (<b>c</b>,<b>d</b>) for the case of grain clusters embedded in randomly oriented grains.</p>
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<p>Schematic of initial microstructure (<b>a</b>) and grain size distribution (<b>b</b>) for the case of various spatial arrangements of grains and various grain boundary properties used in <a href="#sec4dot3-materials-17-03037" class="html-sec">Section 4.3</a>.</p>
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<p>The evolution of average grain size (<b>a</b>), area fraction (<b>b</b>), and grain size distribution (<b>c</b>,<b>d</b>) in the case of various spatial arrangements of grains and various grain boundary properties.</p>
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10 pages, 3245 KiB  
Article
Ultrathin Titanium Dioxide Coating Enables High-Rate and Long-Life Lithium Cobalt Oxide
by Liu Gao, Xin Jin, Zijin Li, Fujie Li, Binghui Xu and Chao Wang
Materials 2024, 17(12), 3036; https://doi.org/10.3390/ma17123036 - 20 Jun 2024
Viewed by 1050
Abstract
Lithium cobalt oxide (LCO) has been widely used as a leading cathode material for lithium-ion batteries in consumer electronics. However, unstable cathode electrolyte interphase (CEI) and undesired phase transitions during fast Li+ diffusivity always incur an inferior stability of the high-voltage LCO [...] Read more.
Lithium cobalt oxide (LCO) has been widely used as a leading cathode material for lithium-ion batteries in consumer electronics. However, unstable cathode electrolyte interphase (CEI) and undesired phase transitions during fast Li+ diffusivity always incur an inferior stability of the high-voltage LCO (HV-LCO). Here, an ultra-thin amorphous titanium dioxide (TiO2) coating layer engineered on LCO by an atomic layer deposition (ALD) strategy is demonstrated to improve the high-rate and long-cycling properties of the HV-LCO cathode. Benefitting from the uniform TiO2 protective layer, the Li+ storage properties of the modified LCO obtained after 50 ALD cycles (LCO-ALD50) are significantly improved. The results show that the average Li+ diffusion coefficient is nearly tripled with a high-rate capability of 125 mAh g−1 at 5C. An improved cycling stability with a high-capacity retention (86.7%) after 300 cycles at 1C is also achieved, far outperforming the bare LCO (37.9%). The in situ XRD and ex situ XPS results demonstrate that the dense and stable CEI induced by the surface TiO2 coating layer buffers heterogenous lithium flux insertion during cycling and prevents electrolyte, which contributes to the excellent cycling stability of LCO-ALD50. This work reveals the mechanism of surface protection by transition metal oxides coating and facilitates the development of long-life HV-LCO electrodes. Full article
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<p>Schematic illustration of the preparation procedure of the TiO<sub>2</sub> layer on LCO by ALD.</p>
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<p>TEM images of (<b>a</b>) bare LCO and (<b>b</b>) LCO-ALD50 after TiO<sub>2</sub> coating. (<b>c</b>) XRD patterns of LCO-ALD50 with Rietveld refinement. (<b>d</b>) FESEM image of LCO-ALD50 and the corresponding EDS images with elements (<b>e</b>) Co, (<b>f</b>) O and (<b>g</b>) Ti. High-resolution O1s XPS spectra of bare (<b>h</b>) LCO and (<b>i</b>) LCO-ALD50. (<b>j</b>) High-resolution Ti2p XPS spectra of LCO-ALD50.</p>
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<p>Electrochemical properties. (<b>a</b>) Rate capability at different C-rates and (<b>b</b>) cycling stability at 1C (1C = 274 mAh g<sup>−1</sup>) of bare LCO, LCO-ALD25, LCO-ALD50, and LCO-ALD100. The 1st, 50th, 100th, 200th and 300th galvanostatic charge/discharge profiles of (<b>c</b>) bare LCO and (<b>d</b>) LCO-ALD50 at 1C. (<b>e</b>) The comparison of cycling performance between LCO-ALD50 and the reported TiO<sub>2</sub>-coated LCO electrodes. (<b>f</b>) Nyquist plots before and after 300 cycles of LCO-ALD50. The 1st, 2nd, 5th and 10th CV curves of (<b>g</b>) bare LCO and (<b>h</b>) LCO-ALD50 measured at 0.1 mV s<sup>−1</sup>.</p>
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<p>Investigation of the excellent surface stability of bare LCO and LCO-ALD50 at 4.5 V. XPS depth spectra of (<b>a</b>) C1s, (<b>b</b>) O1s, and (<b>c</b>) F1s for bare LCO and of (<b>d</b>) C1s, (<b>e</b>) O1s, and (<b>f</b>) F1s for LCO-ALD50 after 100 cycles at 1C.</p>
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<p>FESEM images of (<b>a</b>,<b>b</b>) bare LCO and (<b>c</b>,<b>d</b>) LCO-ALD50 after 300 cycles at 1C.</p>
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13 pages, 9232 KiB  
Article
Impact of Lime Saturation Factor on Alite-Ye’Elimite Cement Synthesis and Hydration
by Xiaodong Li, Bing Ma, Wenqian Ji, Shang Dou, Hao Zhou, Houhu Zhang, Jiaqing Wang, Yueyang Hu and Xiaodong Shen
Materials 2024, 17(12), 3035; https://doi.org/10.3390/ma17123035 - 20 Jun 2024
Viewed by 3647
Abstract
Alite(C3S)-Ye’elimite(C4A3$) cement is a high cementitious material that incorporates a precise proportion of ye’elimite into the ordinary Portland cement. The synthesis and hydration behavior of Alite-Ye’elimite clinker with different lime saturation factors were investigated. The clinkers were [...] Read more.
Alite(C3S)-Ye’elimite(C4A3$) cement is a high cementitious material that incorporates a precise proportion of ye’elimite into the ordinary Portland cement. The synthesis and hydration behavior of Alite-Ye’elimite clinker with different lime saturation factors were investigated. The clinkers were synthesized using a secondary thermal treatment process, and their compositions were characterized. The hydrated pastes were analyzed for their hydration products, pore structure, mechanical strength, and microstructure. The clinkers and hydration products were characterized using XRD, TG-DSC, SEM, and MIP analysis. The results showed that the Alite-Ye’elimite cement clinker with a lime saturation factor (KH) of 0.93, prepared through secondary heat treatment, contained 64.88% C3S and 2.06% C4A3$. At this composition, the Alite-Ye’elimite cement clinker demonstrated the highest 28-day strength. The addition of SO3 to the clinkers decreased the content of tricalcium aluminate (C3A) and the ratio of Alite/Belite (C3S/C2S), resulting in a preference for belite formation. The pore structure of the hydrated pastes was also investigated, revealing a distribution of pore sizes ranging from 0.01 to 10 μm, with two peaks on each differential distribution curve corresponding to micron and sub-micron pores. The pore volume decreased from 0.22 ± 0.03 to 0.15 ± 0.18 cm3 g−1, and the main peak of pore distribution shifted towards smaller sizes with increasing hydration time. Full article
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<p>Clinker disks sintered on Pt slice (<b>a</b>) and the comparison of f-CaO contents at two sintering temperatures (<b>b</b>).</p>
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<p>XRD spectra of clinkers.</p>
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<p>Microscopy images of clinkers before and after secondary annealing at 1270 °C. A is alite, B is belite, Al is aluminate, F is ferrite, L is f-CaO, In is interstitial phases, and B.I is belite inclusion.</p>
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<p>Particle size distribution of clinker powders.</p>
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<p>Compressive strength of the mortars.</p>
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<p>XRD spectra of hydration pastes at 1, 3, and 28 d.</p>
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<p>Heat flow (<b>a</b>) and total heat release (<b>b</b>) of ACSA clinkers.</p>
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<p>Pore volume and porosity distribution of pastes at 1, 3, and 28 d.</p>
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<p>SEM images of MKH hydration pastes at 1 d (<b>a</b>), 3 d (<b>b</b>), and 28 d (<b>c</b>,<b>d</b>).</p>
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16 pages, 2705 KiB  
Article
Oxidation Driven Damage on SiC/BN/SiC Ceramic Matrix Composite Aero-Engine Structures: An Iterative Computational Framework
by Giacomo Canale and Roberto Citarella
Materials 2024, 17(12), 3034; https://doi.org/10.3390/ma17123034 - 20 Jun 2024
Viewed by 566
Abstract
Ceramic matrix composites (CMCs) could be a game changer in the aero-engine industry. Their density is circa one-third of their metallic counterpart. CMCs, furthermore, offer increased strength and greater capability at very high temperatures. This would allow for a reduction in cooling and [...] Read more.
Ceramic matrix composites (CMCs) could be a game changer in the aero-engine industry. Their density is circa one-third of their metallic counterpart. CMCs, furthermore, offer increased strength and greater capability at very high temperatures. This would allow for a reduction in cooling and an increased engine performance. Some challenges, besides the complexity of the manufacturing process, however, remain for the structural integrity of this technology. CMCs are inherently brittle; furthermore, they tend to oxidise when attacked by water or oxygen, and their constituents become brittle and more prone to failure. There are two main points of novelty proposed by this work. The first one is to model and reproduce recent oxidation experimental data with a simple Fick’s law implemented in Abaqus. The parameters of this modelling are a powerful tool for the design of such material systems. The second aspect consists in the development of a new computational framework for iteratively calculating oxygen diffusion and stiffness degradation of the material. Oxidation and stiffness degradation are in fact coupled phenomena. The crack (or microcracking) opening, the function of applied stress, accelerates oxygen diffusion whilst the oxidation diffusion itself contributes to embrittlement and then damage introduction in the material system. Full article
(This article belongs to the Section Advanced and Functional Ceramics and Glasses)
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<p><span class="html-italic">BN</span> interface surrounding the fibres [<a href="#B15-materials-17-03034" class="html-bibr">15</a>].</p>
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<p>Weight uptake specimen taken from the work of Detwiler and Opila [<a href="#B14-materials-17-03034" class="html-bibr">14</a>].</p>
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<p>The Weight Gain Experimental Results for the Geometry of <a href="#materials-17-03034-f002" class="html-fig">Figure 2</a>.</p>
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<p>A quarter of the model is shown. Saturation boundary conditions are applied to the external surface. This is an imposed temperature of 1.03.</p>
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<p>Experimental and Simulation Curves for 800 °C.</p>
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<p>Experimental and Simulation Curves for 600 °C.</p>
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<p>An example of the spatial distribution of the material oxidation (modelled as a temperature) at a given time of the oxidation process.</p>
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<p>An example of stiffness degradation (800 °C, t = 0) as a function of time and oxygen concentration.</p>
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<p>The boundary condition applied to the stress model. The arrows are a graphical representation of the Boundary Condition in Abaqus 6.14.</p>
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<p>The applied load as a negative pressure. The orange symbol is a representation of the Boundary Condition in Abaqus 6.14. The arrow is a graphic representation of the load.</p>
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<p>The illustration of the location of the maximum total strain of the stress model employed to verify the computational framework.</p>
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<p>The total strain evolution during the iterative procedure for three different iteration times.</p>
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<p>The weight uptake evolution during the iterative procedure for three different iteration times.</p>
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<p>The total strain evolution as a function of time for 75 MPa applied pressure.</p>
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<p>The weight uptake evolution as a function of time for 75 MPa applied pressure.</p>
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11 pages, 4161 KiB  
Article
Research and Design of Energy-Harvesting System Based on Macro Fiber Composite Cantilever Beam Applied in Low-Frequency and Low-Speed Water Flow
by Rui Huang, Jingjing Zhou, Jie Shen, Jing Tian, Jing Zhou and Wen Chen
Materials 2024, 17(12), 3033; https://doi.org/10.3390/ma17123033 - 20 Jun 2024
Cited by 1 | Viewed by 686
Abstract
In nature, lakes and water channels offer abundant underwater energy sources. However, effectively harnessing these green and sustainable underwater energy sources is challenging due to their low flow velocities. Here, we propose an underwater energy-harvesting system based on a cylindrical bluff body and [...] Read more.
In nature, lakes and water channels offer abundant underwater energy sources. However, effectively harnessing these green and sustainable underwater energy sources is challenging due to their low flow velocities. Here, we propose an underwater energy-harvesting system based on a cylindrical bluff body and a cantilever beam composed of a macro fiber composite (MFC), taking advantage of the MFC’s low-frequency, lightweight, and high piezoelectric properties to achieve energy harvesting in low-frequency and low-speed water flows. When a water flow impacts the cylindrical bluff body, it generates vibration-enhanced and low-frequency vortices behind the bluff body. The optimized diameter of the bluff body and the distance between the bluff body and the MFC were determined using finite element analysis software, specifically COMSOL. According to the simulation results, an energy-harvesting system based on an MFC cantilever beam applied in a low-frequency and low-speed water flow was designed and prepared. When the diameter of the bluff body was 25 mm, and the distance between the bluff body and MFC was 10 mm and the maximum output voltage was 22.73 V; the power density could reach 0.55 mW/cm2 after matching the appropriate load. The simulation results and experimental findings of this study provide valuable references for designing and investigating energy-harvesting systems applied in low-frequency and low-speed water flows. Full article
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<p>Low-frequency and low-velocity underwater energy harvesting using MFCs: (<b>a</b>) system design, (<b>b</b>) d<sub>33</sub> operating mode of MFC, (<b>c</b>) and mechanism of energy harvesting. Red arrow represents the vibration direction of the MFC.</p>
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<p>Theoretical analysis and modeling of MFC.</p>
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<p>Influence of different distances on MFC energy harvesting: (<b>a</b>) 5 mm, (<b>b</b>) 10 mm, (<b>c</b>) 15 mm, (<b>d</b>) 20 mm, (<b>e</b>) 25 mm, and (<b>f</b>) 30 mm.</p>
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<p>Influence of different diameters on MFC energy harvesting: (<b>a</b>) 10 mm, (<b>b</b>) 15 mm, (<b>c</b>) 20 mm, (<b>d</b>) 25 mm, (<b>e</b>) 27 mm, and (<b>f</b>) 30 mm.</p>
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<p>The electrical output performance of the MFC: (<b>a</b>) the output voltage of the MFC on different substrates, (<b>b</b>) the energy-harvesting performance of the MFC cantilever beam with an aluminum substrate, (<b>c</b>) the influence of MFC energy harvesting, (<b>d</b>) the influence of the parallel resistor on MFC energy harvesting, (<b>e</b>) a comparison of simulated and tested output voltages for different bluff body diameters, and (<b>f</b>) a comparison of simulated and tested output voltages for different distances between the bluff body and the MFC.</p>
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22 pages, 6244 KiB  
Article
Bond Strength Assessment of Normal Strength Concrete–Ultra-High-Performance Fiber Reinforced Concrete Using Repeated Drop-Weight Impact Test: Experimental and Machine Learning Technique
by Sadi I. Haruna, Yasser E. Ibrahim, Ibrahim Hayatu Hassan, Ali Al-shawafi and Han Zhu
Materials 2024, 17(12), 3032; https://doi.org/10.3390/ma17123032 - 20 Jun 2024
Cited by 1 | Viewed by 1172
Abstract
Ultra-high-performance concrete (UHPC) has been used in building joints due to its increased strength, crack resistance, and durability, serving as a repair material. However, efficient repair depends on whether the interfacial substrate can provide adequate bond strength under various loading scenarios. The objective [...] Read more.
Ultra-high-performance concrete (UHPC) has been used in building joints due to its increased strength, crack resistance, and durability, serving as a repair material. However, efficient repair depends on whether the interfacial substrate can provide adequate bond strength under various loading scenarios. The objective of this study is to investigate the bonding behavior of composite U-shaped normal strength concrete–ultra-high-performance fiber reinforced concrete (NSC-UHPFRC) specimens using multiple drop-weight impact testing techniques. The composite interface was treated using grooving (Gst), natural fracture (Nst), and smoothing (Sst) techniques. Ensemble machine learning (ML) algorithms comprising XGBoost and CatBoost, support vector machine (SVM), and generalized linear machine (GLM) were employed to train and test the simulation dataset to forecast the impact failure strength (N2) composite U-shaped NSC-UHPFRC specimen. The results indicate that the reference NSC samples had the highest impact strength and surface treatment played a substantial role in ensuring the adequate bond strength of NSC-UHPFRC. NSC-UHPFRC-Nst can provide sufficient bond strength at the interface, resulting in a monolithic structure that can resist repeated drop-weight impact loads. NSC-UHPFRC-Sst and NSC-UHPFRC-Gst exhibit significant reductions in impact strength properties. The ensemble ML correctly predicts the failure strength of the NSC-UHPFRC composite. The XGBoost ensemble model gave coefficient of determination (R2) values of approximately 0.99 and 0.9643 at the training and testing stages. The highest predictions were obtained using the GLM model, with an R2 value of 0.9805 at the testing stage. Full article
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<p>Schematic procedure for the production of NSC-UHPFRC specimens.</p>
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<p>Surface treatment techniques adopted in this study.</p>
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<p>Multiple drop-weight Impact tests.</p>
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<p>Structure of SVM.</p>
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<p>Flow chart of the model development.</p>
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<p>The impact strength (<span class="html-italic">N</span>1) of NSC-UHPFRC specimens.</p>
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<p>The impact strength (<span class="html-italic">N</span>2) of NSC-UHPFRC specimens.</p>
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<p>(<b>a</b>) Ductility index and (<b>b</b>) COV of the impact strength data.</p>
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<p>Distribution plots of impact test results for NSC: (<b>a</b>) <span class="html-italic">N</span>1 and (<b>b</b>) <span class="html-italic">N</span>2.</p>
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<p>Normal probability plots of impact test results for NSC: (<b>a</b>) <span class="html-italic">N</span>1 (<b>b</b>) <span class="html-italic">N</span>2.</p>
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<p>Distribution plots of NSC-UHPFRC-Nst impact test results: (<b>a</b>) <span class="html-italic">N</span>1 and (<b>b</b>) <span class="html-italic">N</span>2.</p>
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<p>The probability plots of impact test results for NSC-UHPFRC-Nst: (<b>a</b>) <span class="html-italic">N</span>1 (<b>b</b>) <span class="html-italic">N</span>2.</p>
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<p>Distribution plots of NSC-UHPFRC-Sst impact test results: (<b>a</b>) <span class="html-italic">N</span>1 and (<b>b</b>) <span class="html-italic">N</span>2.</p>
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<p>Probability plots of impact test results for NSC-UHPFRC-Sst: (<b>a</b>) <span class="html-italic">N</span>1 (<b>b</b>) <span class="html-italic">N</span>2.</p>
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<p>Distribution plots of NSC-UHPFRC-Gst impact test results: (<b>a</b>) <span class="html-italic">N</span>1 and (<b>b</b>) <span class="html-italic">N</span>2.</p>
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<p>Normal probability plots of impact test results for NSC-UHPFRC-Gst: (<b>a</b>) <span class="html-italic">N</span>1 (<b>b</b>) <span class="html-italic">N</span>2.</p>
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<p>Pearson correlation matrix of the dataset.</p>
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<p>Relative distribution of the dataset parameters.</p>
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<p>Scatter and line plots of the relationship between the predicted <span class="html-italic">N</span>2 and measured <span class="html-italic">N</span>2 values based on the (<b>a</b>) XGBoost, (<b>b</b>) Catboost (<b>c</b>), SVM and (<b>d</b>) GLM models.</p>
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<p>Taylor diagrams displaying model performance: (<b>a</b>) training phase and (<b>b</b>) testing phase.</p>
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<p>Boxplots displaying relative error distributions: (<b>a</b>) training and (<b>b</b>) testing stages.</p>
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12 pages, 9391 KiB  
Article
The Influence of Heat Treatment on the Microstructure and Properties of a Cu-Bearing Ultra-Low Carbon Steel
by Weina Zhang, Zhanjie Gao, Huimin Zhang, Hao Wei, Zejin Chen, Wenying Xue and Zhenyu Liu
Materials 2024, 17(12), 3031; https://doi.org/10.3390/ma17123031 - 20 Jun 2024
Cited by 1 | Viewed by 841
Abstract
This study reveals the relationship between the Cu precipitates and mechanical properties of a Cu-baring ultra-low carbon steel after two-phase zone quenching and tempering at 923 K for 0.5–2.5 h. The tensile and microstructural properties were investigated as a function of heat treatment [...] Read more.
This study reveals the relationship between the Cu precipitates and mechanical properties of a Cu-baring ultra-low carbon steel after two-phase zone quenching and tempering at 923 K for 0.5–2.5 h. The tensile and microstructural properties were investigated as a function of heat treatment time. The contribution of the precipitation-strengthening mechanism to yield strength was calculated. The size, morphology, and distribution of the precipitated particles were observed using TEM. As the heat treatment time increased, the strength gradually decreased and then remained stable, and the elongation gradually increased and then remained stable. Additionally, the contributions of each strengthening mechanism to the yield strength under different heat treatments were 117, 107, 102, and 89 MPa, respectively. The size and quantity of the precipitates increased with the increase in heat treatment time. After tempering for more than 2 h, the precipitates continued to coarsen, but their quantity decreased. The precipitated Cu had a 3R structure with a length of approximately 17.1 nm and a width of approximately 9.7 nm, with no twinning inside. The stacking order was ABC/ABC. The stable Cu precipitation structure was FCC, maintaining a K-S orientation relationship 11¯1FCC Cu //(0 1 1) α, 1¯10FCC Cu//[11¯1] α. Full article
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<p>Heat treatment process of the experimental steel.</p>
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<p>Tensile properties of the experimental steel under different heat treatment conditions: (<b>a</b>) typical stretch curve; (<b>b</b>) tensile properties change trend.</p>
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<p>OM and SEM images of microstructure under different heat treatment conditions: (<b>a</b>,<b>b</b>) 0.5 h, (<b>c</b>,<b>d</b>) 1 h, (<b>e</b>,<b>f</b>) 2 h, and (<b>g</b>,<b>h</b>) 2.5 h.</p>
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<p>TEM images of microstructure under different heat treatment conditions: (<b>a</b>) 0.5 h, (<b>b</b>) 1 h, (<b>c</b>) 2 h, and (<b>d</b>) 2.5 h.</p>
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<p>Statistical analysis of precipitation particle size under different heat treatment conditions: (<b>a</b>,<b>b</b>) 0.5 h, (<b>c</b>,<b>d</b>) 1 h, (<b>e</b>,<b>f</b>) 2 h, and (<b>g</b>,<b>h</b>) 2.5 h.</p>
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<p>High-resolution image analysis of 3R Cu at 650 °C for 2 h. (<b>a</b>) 3R Cu image, (<b>b</b>) the FFT pattern of (<b>a</b>), (<b>c</b>) IFFT image after filtrating of 3R Cu.</p>
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<p>HRTEM analysis of ellipsoidal FCC Cu at 650 °C for 2 h. (<b>a</b>) FCC Cu image, (<b>b</b>) the FFT pattern of (<b>a</b>), (<b>c</b>) IFFT image after filtrating of matrix.</p>
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15 pages, 4861 KiB  
Article
Optimization of Vertical Fixed-Bed Pyrolysis for Enhanced Biochar Production from Diverse Agricultural Residues
by Tasi-Jung Jiang, Hervan Marion Morgan, Jr. and Wen-Tien Tsai
Materials 2024, 17(12), 3030; https://doi.org/10.3390/ma17123030 - 20 Jun 2024
Viewed by 1014
Abstract
This study examines the pyrolysis of agricultural residues, namely, coconut shells, rice husks, and cattle manure, in a vertical fixed-bed reactor at varying temperatures from 300 to 800 degrees Celsius for biochar production. The research aimed to evaluate the potential of biochar as [...] Read more.
This study examines the pyrolysis of agricultural residues, namely, coconut shells, rice husks, and cattle manure, in a vertical fixed-bed reactor at varying temperatures from 300 to 800 degrees Celsius for biochar production. The research aimed to evaluate the potential of biochar as biofuels, adsorbents, and soil amendments. Proximate, ultimate, and elemental analyses were conducted to determine their composition and caloric values. Several analytical techniques were used in the physical and chemical characterization of the biochar (SEM, FTIR, BET). The results indicated that the highest SBET values were achieved under different conditions for each biochar: 89.58 m2/g for BC-CS-700, 202.39 m2/g for BC-RH-600, and 42.45 m2/g for BC-CD-800. Additionally, all three biochars exhibited the highest caloric values at 600 °C. The results showed that 600 °C is the general optimal temperature to produce biochar from an assortment of biomass materials, considering their use for a variety of purposes. BC-CS-800 had the highest elemental carbon content at 93%, accompanied by a relative decrease in oxygen content. The van Krevelen diagram of biochar products shows that biochars derived from coconut shells and rice husks are suitable for use as fuels. Furthermore, FTIR analysis revealed the presence of oxygen-containing functional groups on the biochar surface, enhancing their pollutant adsorption capabilities. This study provides valuable insights into the scalable and environmentally sustainable production of biochar, emphasizing its role in improving soil quality, increasing energy density, and supporting sustainable agricultural practices. Full article
(This article belongs to the Special Issue Green Materials and Manufacturing Processes (2nd Edition))
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<p>TGA and DTG curves of the three biomass samples (CS, RH, and CD) recorded at a constant rate of 10 °C/min.</p>
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<p>SEM images of CS biochar. (<b>a</b>) BC/CS-300 (left); (<b>b</b>) BC/CS-800-0 (right).</p>
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<p>SEM images of RH biochar. (<b>a</b>) BC/RH-300 (left); (<b>b</b>) BC/RH-800-0 (right).</p>
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<p>SEM images of CD biochar. (<b>a</b>) BC/CD-300 (left); (<b>b</b>) BC/CD-800-0 (right).</p>
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<p>Ultimate analysis of the raw biomass and biochars (800 °C).</p>
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<p>The van Krevelen diagram of the raw biomass and biochar (800 °C).</p>
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<p>FTIR spectra of the resulting biochar (800 °C).</p>
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13 pages, 1335 KiB  
Article
New Methodology for Modifying Sodium Montmorillonite Using DMSO and Ethyl Alcohol
by Adriana Stoski, Bruno Rafael Machado, Bruno Henrique Vilsinski, Lee Marx Gomes de Carvalho, Edvani Curti Muniz and Carlos Alberto Policiano Almeida
Materials 2024, 17(12), 3029; https://doi.org/10.3390/ma17123029 - 20 Jun 2024
Viewed by 823
Abstract
Modified clays with organic molecules have many applications, such as the adsorption of pollutants, catalysts, and drug delivery systems. Different methodologies for intercalating these structures with organic moieties can be found in the literature with many purposes. In this paper, a new methodology [...] Read more.
Modified clays with organic molecules have many applications, such as the adsorption of pollutants, catalysts, and drug delivery systems. Different methodologies for intercalating these structures with organic moieties can be found in the literature with many purposes. In this paper, a new methodology of modifying Sodium Montmorillonite clays (Na-Mt) with a faster drying time was investigated by X-ray diffraction (XRD), Fourier transform infrared spectroscopy (FTIR), BET, and thermogravimetric analysis (TG and DTG). In the modification process, a mixture of ethyl alcohol, DMSO, and Na-Mt were kept under magnetic stirring for one hour. Statistical analysis was applied to evaluate the effects of the amount of DMSO, temperature, and sonication time on the modified clay (DMSO-SMAT) using a 23-factorial design. XRD and FTIR analyses showed the DMSO intercalation into sodium montmorillonite Argel-T (SMAT). An average increase of 0.57 nm for the interplanar distance was found after swelling with DMSO intercalation. BET analysis revealed a decrease in the surface area (from 41.8933 m2/g to 2.1572 m2/g) of Na-Mt when modified with DMSO. The porosity increased from 1.74 (SMAT) to 1.87 nm (DMSO-SMAT) after the application of the methodology. Thermal analysis showed a thermal stability for the DMSO-SMAT material, and this was used to calculate the DMSO-SMAT formula of Na[Al5Mg]Si12O30(OH)6 · 0.54 DMSO. Statistical analysis showed that only the effect of the amount of DMSO was significant for increasing the interlayer space of DMSO-SMAT. In addition, at room temperature, the drying time of the sample using this methodology was 30 min. Full article
(This article belongs to the Section Materials Chemistry)
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<p>XRD patterns of unmodified Mt (SMAT) and modified Mt (DMSO-SMAT) samples.</p>
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<p>FTIR spectra of modified Mt (DMSO-SMAT) and unmodified Mt (SMAT) samples with emphasis on the region between 960 and 900 cm<sup>−1</sup>.</p>
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<p>TG and DTG curves for modified Mt (DMSO-SMAT) and unmodified Mt (SMAT) samples.</p>
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<p>Interaction effects between: (<b>a</b>) temperature and amount of the DMSO; (<b>b</b>) temperature and sonication time and (<b>c</b>) amount of the DMSO and sonication time for the 2<sup>3</sup>-factorial designs for interplanar space increase.</p>
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<p>Appearance of the samples using the procedure of <a href="#sec2dot2-materials-17-03029" class="html-sec">Section 2.2</a>: (<b>a</b>) 10 min and (<b>b</b>) 30 min of drying with ethanol; (<b>c</b>) 10 min and (<b>d</b>) 30 min without ethanol.</p>
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16 pages, 6145 KiB  
Article
Electrochemical Impedance Spectroscopy Analysis of Organic Epoxy Coatings Reinforced with Nano Clay
by Davide Asperti, Marina Cabrini, Sergio Lorenzi, Giuseppe Rosace, Abdollah Omrani and Tommaso Pastore
Materials 2024, 17(12), 3028; https://doi.org/10.3390/ma17123028 - 20 Jun 2024
Viewed by 829
Abstract
Electrochemical impedance spectroscopy (EIS) is a modern and efficient method for the evaluation of the protective abilities of coatings. However, the interpretation of the experimental data is a difficult task. This paper aims to investigate the effect of the addition of a nano [...] Read more.
Electrochemical impedance spectroscopy (EIS) is a modern and efficient method for the evaluation of the protective abilities of coatings. However, the interpretation of the experimental data is a difficult task. This paper aims to investigate the effect of the addition of a nano clay, Cloesite 30B®, on the barrier properties of an epoxy-based system through electrochemical impedance spectroscopy in an aerated sodium chloride solution. The EIS spectra of the samples analysed showed different evolutions over time. The subsequent processing of spectra using equivalent electrical circuits is an excellent analytical tool and allows the protective capacity of coatings to be assessed. By using this analysis, it was possible to define and comprehend the impact of adding nano clay in different concentrations to the epoxy resin coating. The work has shown the effectiveness of increasing the barrier effect of the coating with this type of nano clay. However, the improvement is linked to obtaining a correct dispersion of nanoparticles. Otherwise, there is the formation of macro-clusters of particles inside the coating. Their appearance can cause a deterioration in coating performance. Full article
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<p>Chemical structure and physical properties of Cloisite 30B<sup>®</sup>.</p>
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<p>(<b>a</b>) SEM image of a macro-cluster of nano clay particles; (<b>b</b>) detail of the macro-cluster.</p>
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<p>Roughness analysis of pickled surface by confocal interferometric profilometer.</p>
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<p>Surfaces of specimens after 1000 h of immersion in NaCl 3.5% solution; (<b>a</b>,<b>b</b>) Specimens with epoxy resin coating; (<b>c</b>,<b>d</b>) Specimens with 1 wt% of nanoclay; (<b>e</b>,<b>f</b>) Specimens with 3 wt% of nanoclay; (<b>g</b>,<b>h</b>) Specimens with 5 wt% of nanoclay.</p>
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<p>Bode diagrams after 1000 h exposure in 3.5% NaCl solution.</p>
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<p>Evolution of EIS spectra during 1000 h exposure in 3.5% NaCl solution.</p>
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<p>Equivalent electrical circuits used: (<b>a</b>) E.C. with one-time constant; (<b>b</b>) E.C. with two-time constants; (<b>c</b>) E.C. with two-time constants and Warburg impedance; (<b>d</b>) E.C. with three-time constants.</p>
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<p>(<b>a</b>) Coating capacity, C<sub>c</sub>∙d<sub>n</sub>, during the entire exposure period; (<b>b</b>) average coating capacity, C<sub>c</sub>∙d<sub>n,</sub> of specimens with and without nano clay inside the coating during the entire exposure period.</p>
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<p>EIS spectra and EEC after (<b>a</b>) 2 h and (<b>b</b>) 135 h exposure for specimen B1 with 1 wt% of nanoparticles.</p>
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<p>EIS spectra after 235 h and 1000 h exposure for specimen B1 with 1 wt% of nanoparticles.</p>
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<p>EIS spectra after (<b>a</b>) 70 h and (<b>b</b>) 135 h exposure for specimen D2 with 5 wt% of nanoparticles.</p>
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<p>EIS spectra and EEC after (<b>a</b>) 2 h and (<b>b</b>) 235 h exposure for specimen A2 with 0 wt% of the nanoparticles.</p>
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<p>EIS spectra and EEC after 1000 h exposure for specimen A2 with 0 wt% of the nanoparticles.</p>
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<p>EIS spectra and EEC after (<b>a</b>) 70 h and (<b>b</b>) 1000 h exposure for specimen C2 with 3 wt% of nanoparticles.</p>
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<p>Electrical resistivity, ρ, variation over time compared with the value of ρ<sub>e</sub>.</p>
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<p>EDS analysis of a nano clay cluster in the coating with 3 wt% addition of Cloisite 30B<sup>®</sup>.</p>
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15 pages, 12866 KiB  
Article
Utilization Potential of Aerated Concrete Block Powder and Coffee Grounds Ash in Green-Growing Concrete
by Jinping Li, Rong Huang, Zheng Chen, Xuedi Sun and Deliang Yu
Materials 2024, 17(12), 3027; https://doi.org/10.3390/ma17123027 - 20 Jun 2024
Viewed by 817
Abstract
The purpose of this research is to investigate the utilization potential of recycled powder made from spent coffee grounds (SCGs) and aerated concrete blocks (ACBs) in green-growing concrete. The green-growing concrete is prepared using ACB powder and SCG ash as raw materials instead [...] Read more.
The purpose of this research is to investigate the utilization potential of recycled powder made from spent coffee grounds (SCGs) and aerated concrete blocks (ACBs) in green-growing concrete. The green-growing concrete is prepared using ACB powder and SCG ash as raw materials instead of 5%, 15%, and 25% and 5%, 10%, and 15% cement, respectively. Then, the two raw materials are compounded with the optimal content. The compressive strength and alkalinity of green-growing concrete at 7d and 28d and the frost resistance after 25 freeze–thaw cycles at 28d are studied. The results showed that the optimum content of ACB powder and SCG ash was 5%. Replacing 5% cement with recycled powder could improve the strength of concrete. The alkalinity of concrete containing ACB powder gradually increased, while the alkalinity of concrete containing SCG ash gradually decreased. The alkalinity of ACB-SCG powder was lower than that of ACB powder but slightly higher than that of SCG ash. The frost resistance of concrete containing ACB powder decreased gradually, and the frost resistance of concrete containing SCG ash increased first and then decreased greatly. The frost resistance of ACB-SCG powder could neutralize that of ACB powder and SCG ash. Full article
(This article belongs to the Section Construction and Building Materials)
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<p>ACB powder and SCG ash diagram and SEM diagram: (<b>a</b>) ACB powder; (<b>b</b>) SCG ash; (<b>c</b>) the SEM of ACB powder; and (<b>d</b>) the SEM of SCG ash.</p>
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<p>The FTIR test of recycled fine powder concrete.</p>
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<p>Flow process chart.</p>
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<p>Flow chart of frost resistance of regenerated powder in green−growing concrete.</p>
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<p>The porosity of recycled fine powder concrete.</p>
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<p>The compressive strength of concrete with recycled fine powder.</p>
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<p>Alkalinity of recycled fine powder concrete.</p>
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<p>Frost resistance of recycled fine powder concrete. (<b>a</b>) Strength loss rate. (<b>b</b>) Mass loss rate.</p>
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<p>Micromorphology of concrete containing recycled fine powder: (<b>a</b>) optical microscope photo of ACB particle; (<b>b</b>) interface transition zone between ACB particle and cement paste; (<b>c</b>) optical microscope photo of SCG ash; (<b>d</b>) interface transition zone between SCG ash and cement paste; (<b>e</b>) optical microscope photo of ACB-SCG powder; and (<b>f</b>) interface transition zone between ACB-SCG powder and cement paste.</p>
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18 pages, 5495 KiB  
Article
Accelerated Design for Perovskite-Oxide-Based Photocatalysts Using Machine Learning Techniques
by Xiuyun Zhai and Mingtong Chen
Materials 2024, 17(12), 3026; https://doi.org/10.3390/ma17123026 - 20 Jun 2024
Viewed by 952
Abstract
The rapid discovery of photocatalysts with desired performance among tens of thousands of potential perovskites represents a significant advancement. To expedite the design of perovskite-oxide-based photocatalysts, we developed a model of ABO3-type perovskites using machine learning methods based on atomic and [...] Read more.
The rapid discovery of photocatalysts with desired performance among tens of thousands of potential perovskites represents a significant advancement. To expedite the design of perovskite-oxide-based photocatalysts, we developed a model of ABO3-type perovskites using machine learning methods based on atomic and experimental parameters. This model can be used to predict specific surface area (SSA), a key parameter closely associated with photocatalytic activity. The model construction involved several steps, including data collection, feature selection, model construction, web-service development, virtual screening and mechanism elucidation. Statistical analysis revealed that the support vector regression model achieved a correlation coefficient of 0.9462 for the training set and 0.8786 for the leave-one-out cross-validation. The potential perovskites with higher SSA than the highest SSA observed in the existing dataset were identified using the model and our computation platform. We also developed a webserver of the model, freely accessible to users. The methodologies outlined in this study not only facilitate the discovery of new perovskites but also enable exploration of the correlations between the perovskite properties and the physicochemical features. These findings provide valuable insights for further research and applications of perovskites using machine learning techniques. Full article
(This article belongs to the Section Materials Simulation and Design)
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<p>A schematic illustration of the crystal cell of a typical ABO<sub>3</sub>-type perovskite.</p>
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<p>An illustration of the six steps involved in the construction of the model.</p>
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<p>Feature screening using (<b>a</b>) FSM-SVR, (<b>b</b>) BSM-SVR, and (<b>c</b>) GA-SVR. The blue and red circles represent RMSE and the minimum RMSE, respectively. In the illustration, the green and orange circles represent RMSE and Score, respectively.</p>
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<p>RMSE versus γ and ε obtained in the optimization process of the algorithm hyperparameters.</p>
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<p>The experimental versus predicted SSA of the samples in (<b>a</b>) the training set; (<b>b</b>) LOOCV; (<b>c</b>) the testing set.</p>
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<p>A screenshot of the web service for predicting SSA of ABO<sub>3</sub>-type perovskites.</p>
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<p>Virtual screening of ABO<sub>3</sub>-type perovskites.</p>
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<p>The relationships between SSA and the key features. (<b>a</b>) Calcination time and Drying temperature; (<b>b</b>) Melting point of B-site and Density of A-site; (<b>c</b>) <b><span class="html-italic">P<sub>CA</sub></span><sub>3</sub></b> and <b><span class="html-italic">P<sub>CA</sub></span><sub>6</sub></b>; (<b>d</b>) Electron affinity of A-site and Electron affinity of B-site.</p>
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<p>The projection of pattern recognition.</p>
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15 pages, 6410 KiB  
Article
Effects of High Al Content on the Phase Constituents and Thermal Properties in NiCoCrAlY Alloys
by Jin Zhang, Zhihua Nie, Chengpeng Tan, Rende Mu, Shilei Li, Xianjin Ning and Chengwen Tan
Materials 2024, 17(12), 3025; https://doi.org/10.3390/ma17123025 - 20 Jun 2024
Viewed by 831
Abstract
MCrAlY (M = Ni and/or Co) metallic coatings are essential for the protection of hot-end components against thermal and corrosion damage. Increasing the Al content is considered a feasible solution to improve the high-temperature performance of MCrAlY coatings. In this paper, the effects [...] Read more.
MCrAlY (M = Ni and/or Co) metallic coatings are essential for the protection of hot-end components against thermal and corrosion damage. Increasing the Al content is considered a feasible solution to improve the high-temperature performance of MCrAlY coatings. In this paper, the effects of high Al contents (12–20 wt.%) on the phase constituents and cast microstructures in MCrAlY alloys were studied by high-energy X-ray diffraction and electron microscopy techniques combined with phase equilibria calculations. High Al content improved the stability of β, σ, and α phases. Meanwhile, an evolution of the cast microstructure morphology from a dendrite structure to an equiaxed grain structure was observed. The thermal properties were analyzed, which were closely related to the phase constituents and solid-to-solid phase transitions at evaluated temperatures. This work is instructive for developing high-Al-content MCrAlY coatings for next-generation thermal barrier applications. Full article
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<p>Calculated equilibrium phase fraction versus temperature curves for the Ni-27.5Co-17Cr-xAl-0.5Y (wt.%) alloys supplemented with 12 wt.% Al (<b>a</b>), 16 wt.% Al (<b>b</b>), and 20 wt.% Al (<b>c</b>). The <span class="html-italic">y</span>-axis represents the mole fraction of each phase at a given temperature.</p>
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<p>HE-XRD patterns of as-cast 12Al, 16Al, and 20Al alloys. (<b>b</b>) is the magnified view of (<b>a</b>).</p>
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<p>HE-XRD patterns of 12Al (<b>a</b>), 16Al (<b>b</b>), and 20Al (<b>c</b>) alloys quenched at different temperatures.</p>
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<p>Microstructure of as-cast 12Al (<b>a</b>–<b>c</b>), 16Al (<b>d</b>–<b>f</b>), and 20Al (<b>g</b>–<b>i</b>) alloys. (<b>a</b>,<b>d</b>,<b>g</b>) are OM images at 50×. (<b>b</b>,<b>c</b>,<b>e</b>,<b>f</b>,<b>h</b>,<b>i</b>) are SEM-BSE images. Magnification increases from left to right.</p>
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<p>EBSD mappings of as-cast 12Al (<b>a</b>,<b>d</b>), 16Al (<b>b</b>,<b>e</b>), and 20Al (<b>c</b>,<b>f</b>) alloys. (<b>a</b>–<b>c</b>) are inverse pole figure maps and (<b>d</b>–<b>f</b>) are phase maps.</p>
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<p>TEM images and the SAED patterns of minor phases in as-cast 12Al (<b>a</b>–<b>c</b>), 16Al (<b>d</b>,<b>e</b>), and 20Al (<b>f</b>) alloys.</p>
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<p>SEM-BSE images of 12Al alloys quenched at 600 °C (<b>a</b>), 800 °C (<b>b</b>), 1000 °C (<b>c</b>), 1100 °C (<b>d</b>), 1200 °C (<b>e</b>), and 1300 °C (<b>f</b>).</p>
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<p>SEM-BSE images of 16Al alloys quenched at 600 °C (<b>a</b>), 800 °C (<b>b</b>), 1000 °C (<b>c</b>), 1100 °C (<b>d</b>), 1200 °C (<b>e</b>), and 1300 °C (<b>f</b>).</p>
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<p>SEM-BSE images of 20Al alloys quenched at 600 °C (<b>a</b>), 800 °C (<b>b</b>), 1000 °C (<b>c</b>), 1100 °C (<b>d</b>), 1200 °C (<b>e</b>), and 1300 °C (<b>f</b>).</p>
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<p>(<b>a</b>) DSC curves of 12Al, 16Al, and 20Al alloys. (<b>b</b>) Plots of coefficient of thermal expansion for 12Al, 16Al, and 20Al alloys as a function of temperature. The CTE values of the γ and β phases are inserted in (<b>b</b>) [<a href="#B27-materials-17-03025" class="html-bibr">27</a>].</p>
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<p>Schematic diagrams of the liquid-to-solid and solid-to-solid phase transitions in the casting process for 12Al, 16Al and 20Al alloys.</p>
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17 pages, 9927 KiB  
Article
Experimental Studies of the Machinability of SiCp/Al with Different Volume Fractions under Ultrasonic-Assisted Grinding
by Chen Hu, Yongwei Zhu and Ruoxun Fan
Materials 2024, 17(12), 3024; https://doi.org/10.3390/ma17123024 - 20 Jun 2024
Cited by 1 | Viewed by 577
Abstract
High-volume fraction silicon carbide particle-reinforced aluminum (SiCp/Al) has a promising application for its high specific strength, wear resistance, and thermal conductivity. However, SiCp/Al components with a high-volume fraction are prone to poor surface quality and defects such as fractures, cracks, and micro-pits. It [...] Read more.
High-volume fraction silicon carbide particle-reinforced aluminum (SiCp/Al) has a promising application for its high specific strength, wear resistance, and thermal conductivity. However, SiCp/Al components with a high-volume fraction are prone to poor surface quality and defects such as fractures, cracks, and micro-pits. It has been reported that ultrasonic-assisted grinding machining (UAG) helps to improve the quality of SiCp/Al machined surfaces. However, the differences between SiCp/Al with different volume fractions obtained by UAG machining are not clear. Therefore, a comparative study of surface roughness, morphology, and cutting force was carried out by UAG machining on SiCp/Al samples with volume fractions of 45% and 60%. Compared to the 45% volume fraction SiCp/Al, the 60% volume fraction SiCp/Al has a higher cutting force and roughness under the same machining parameters. In addition, experiments have shown that cutting forces and surface roughness can be reduced by increasing the tool speed or decreasing the feed rate. UAG machining with an ultrasonic amplitude within 4 μm can also reduce cutting forces and surface roughness. However, more than 6 μm ultrasonic amplitude may lead to an increase in roughness. This study contributes to reasonable parameter settings in ultrasonically-assisted grinding of SiCp/Al with different volume fractions. Full article
(This article belongs to the Section Manufacturing Processes and Systems)
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<p>(<b>a</b>) Material schematic; (<b>b</b>) Sample appearance; (<b>c</b>) Microscopic morphology.</p>
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<p>Schematic diagram of UAG processing.</p>
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<p>Experimental equipment.</p>
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<p>Grinding tool: (<b>a</b>) Schematic diagram of tool structure; (<b>b</b>) Morphology of grinding head.</p>
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<p>Principle of cutting force measurement.</p>
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<p>(<b>a</b>) EDS analysis of sample A after UAG machining with 4 μm. (<b>b</b>) Distribution of elements.</p>
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<p>SEM morphology: (<b>a</b>) surface of sample A by CG machining; (<b>b</b>) surface of sample A by UAG machining with 4 μm amplitude; (<b>c</b>) surface of sample B by UAG machining with 4 μm amplitude.</p>
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<p>SEM morphology of sample B machined by UAG with 8 μm amplitude.</p>
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<p>Morphology of the inlet edge of each machining group.</p>
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<p>(<b>a</b>) Effects of <span class="html-italic">v<sub>s</sub></span> on cutting forces; (<b>b</b>) Effects of <span class="html-italic">v<sub>w</sub></span> on cutting forces.</p>
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<p>(<b>a</b>) Effects of <span class="html-italic">a<sub>p</sub></span> on cutting forces; (<b>b</b>) Effects of <span class="html-italic">A<sub>z</sub></span> on cutting forces.</p>
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<p>Effects of <span class="html-italic">v<sub>s</sub></span> on Ra.</p>
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<p>Effects of <span class="html-italic">v<sub>w</sub></span> on Ra.</p>
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<p>Effects of <span class="html-italic">A<sub>z</sub></span> on Ra different.</p>
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<p>Simulation of abrasive grain trajectory.</p>
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<p>Material removal mechanism in 5 different cases.</p>
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16 pages, 18963 KiB  
Article
Separation of Damage Mechanisms in Full Forward Rod Extruded Case-Hardening Steel 16MnCrS5 Using 3D Image Segmentation
by Lars A. Lingnau, Johannes Heermant, Johannes L. Otto, Kai Donnerbauer, Lukas M. Sauer, Lukas Lücker, Marina Macias Barrientos and Frank Walther
Materials 2024, 17(12), 3023; https://doi.org/10.3390/ma17123023 - 20 Jun 2024
Cited by 2 | Viewed by 741
Abstract
In general, formed components are lightweight as well as highly economic and resource efficient. However, forming-induced ductile damage, which particularly affects the formation and growth of pores, has not been considered in the design of components so far. Therefore, an evaluation of forming-induced [...] Read more.
In general, formed components are lightweight as well as highly economic and resource efficient. However, forming-induced ductile damage, which particularly affects the formation and growth of pores, has not been considered in the design of components so far. Therefore, an evaluation of forming-induced ductile damage would enable an improved design and take better advantage of the lightweight nature as it affects the static and dynamic mechanical material properties. To quantify the amount, morphology and distribution of the pores, advanced scanning electron microscopy (SEM) methods such as scanning transmission electron microscopy (STEM) and electron channeling contrast imaging (ECCI) were used. Image segmentation using a deep learning algorithm was applied to reproducibly separate the pores from inclusions such as manganese sulfide inclusions. This was achieved via layer-by-layer ablation of the case-hardened steel 16MnCrS5 (DIN 1.7139, AISI/SAE 5115) with a focused ion beam (FIB). The resulting images were reconstructed in a 3D model to gain a mechanism-based understanding beyond the previous 2D investigations. Full article
(This article belongs to the Section Advanced Materials Characterization)
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<p>Workflow of the separation of damage mechanisms of components formed via full forward rod extrusion.</p>
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<p>Diagram of fatigue specimen geometry and removal area from the component formed via full forward rod extrusion (all dimensions in mm) based on Möhring [<a href="#B22-materials-17-03023" class="html-bibr">22</a>].</p>
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<p>(<b>a</b>) Load collective for uniaxial fatigue tests; (<b>b</b>) total strain and rotational angle collectives for axial–torsional fatigue tests.</p>
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<p>(<b>a</b>) Schematic representation of the resistance measurement system and (<b>b</b>) the schematic illustration of the ‘delta mode’.</p>
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<p>(<b>a</b>) Example of segmented pores from an SE image (marked in red) and (<b>b</b>) an example of segmented sulfides (marked in red) from an Inlens image of the same slice of the image stack.</p>
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<p>Processing of the FIB-SEM Inlens images.</p>
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<p>(<b>a</b>) Illustration of the milling process and (<b>b</b>) further lamella preparation for the STEM investigations.</p>
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<p>(<b>a</b>) Shoulder-opening-angle-dependent material responses of axial–torsional tested specimens and (<b>b</b>) an exemplary representation of the absolute resistance and the plastic strain amplitude of an axial tested specimen with a shoulder opening angle of 2α = 30°.</p>
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<p>(<b>a</b>) Macroscopic fracture surface of a full forward rod extruded specimen with a shoulder opening angle of 2α = 30° after axial–torsional fatigue stress and fractographic images of (<b>b</b>) ductile fracture areas and (<b>c</b>) the crack initiation near MnS inclusions (marked in red); (<b>d</b>) macroscopic fracture surface of a full forward rod extruded specimen with a shoulder opening angle of 2α = 30° after axial fatigue stress and fractographic images of (<b>e</b>) ductile fracture areas and (<b>f</b>) MnS inclusions on the fracture area.</p>
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<p>AFM measurement of pores inside MnS inclusions (marked in red) of full forward rod extruded case-hardening steel 16MnCrS5 (DIN 1.7139; AISI/SAE 5115) before fatigue testing and the corresponding AFM line profile recorded with Akiyama probes in single-pass tapping mode.</p>
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<p>AFM measurement of nanopores (marked in red) in the perlite phases of full forward rod extruded case-hardening steel 16MnCrS5 (DIN 1.7139; AISI/SAE 5115) before fatigue testing.</p>
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<p>(<b>a</b>) ECCI images of nanopores in the ferrite and (<b>b</b>) perlite phases of full forward rod extruded case-hardening steel 16MnCrS5 (DIN 1.7139; AISI/SAE 5115) before fatigue testing.</p>
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<p>(<b>a</b>) Overview STEM image of the FIB lamella and (<b>b</b>) STEM image of the dislocations in the pearlite phase of full forward rod extruded case-hardening steel 16MnCrS5 (DIN 1.7139; AISI/SAE 5115) before fatigue testing.</p>
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<p>Rendered 3D CAD of (<b>a</b>) pore distribution, (<b>b</b>) sulfide distribution, (<b>c</b>) combined distribution of pores and sulfides, and (<b>d</b>) magnified section of the combined distribution of pores and sulfides of full forward rod extruded case-hardening steel 16MnCrS5 (DIN 1.7139; AISI/SAE 5115) before fatigue testing.</p>
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18 pages, 5764 KiB  
Article
The Potential Risk of Nanoparticulate Release from Photocatalytic Pavement Concrete Surface Due to a Simulated Abrasion Load—An Experimental Study
by Hubert Witkowski, Janusz Jarosławski, Artur Szkop, Karol Chilmon, Maciej Kalinowski and Wioletta Jackiewicz-Rek
Materials 2024, 17(12), 3022; https://doi.org/10.3390/ma17123022 - 20 Jun 2024
Cited by 2 | Viewed by 1034
Abstract
The risk of the releasing of nanometric particles from construction materials with nanometric components might be one of the biggest threats to further development of them. One of the possible ingress routes to human organisms is the respiratory system. Therefore, it is crucial [...] Read more.
The risk of the releasing of nanometric particles from construction materials with nanometric components might be one of the biggest threats to further development of them. One of the possible ingress routes to human organisms is the respiratory system. Therefore, it is crucial to determine the risk of emission of nanometric particles during material usage. In the presented paper, abrasion of mortar samples with nanometric TiO2 was investigated. A special abrasion test setup was developed to reflect everyday abrasion of the concrete surface of pavements. In the study, three TiO2-modifed mortar series (and respective reference series) underwent the developed test protocol and the grains were mobilized from their surface due to the applied load analyzed (granulation, morphology, and chemical composition). For a comparative analysis, an abrasion parameter was developed. Based on the obtained results, the modification of cementitious composites with nanometric TiO2 contributed to a reduction in the emission of aerosols and, therefore, confirmed the compatibility between TiO2 and cement matrix. Full article
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<p>The relative granulations (q) for cement CEM 42.5 R, micro-silica, and quartz powder that were used in the study.</p>
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<p>Morphology of agglomerated nanometric photocatalytic materials used in the study: TiO<sub>2</sub> (A)—micrograph (<b>a</b>); TiO<sub>2</sub> (B)—micrograph (<b>b</b>). TEM analysis performed on copper grids covered with a carbon film (microscope—TEM Tecnai TF 20 X-TWIN; parameters—EDAX, voltage 200 kV, STEM images collected using the HAADF detector).</p>
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<p>A schematic diagram of the experimental setup applied in the research of particle size analysis: (1) HEPA filter, (2) plexiglass chamber, (3) crockmeter, (4) grinding cloth, (5) tested sample, (6) air with particle inlet, (7) flow meter, (8) Scanning Mobility Particle Sizer, (9) Aerodynamic Particle Sizer.</p>
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<p>An example of a comparison of grain diameter distribution. Figure on the <b>top</b>—results of the reference’s sample abrasion (blue) vs. results background (green). Figure on the <b>bottom</b>—results presented as an abrasion parameter value (APV).</p>
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<p>Comparison of grain diameter distribution for grains emitted during the abrasion test. APV values for mortar sample M1—reference (blue) vs. TiO<sub>2</sub>-modified samples (red) for grain diameters of 10.4 ÷ 469.8 nm.</p>
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<p>Comparison of grain diameter distribution for grains emitted during the abrasion test. APV values for mortar sample M1—reference (blue) vs. TiO<sub>2</sub>-modified samples (red) for grain diameters of 0.523 ÷ 19.810 μm.</p>
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<p>Comparison of grain diameter distribution for grains emitted during the abrasion test. APV values for mortar sample M3—reference (blue) vs. TiO<sub>2</sub>-modified samples (red) for grain diameters of 10.4 ÷ 469.8 nm.</p>
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<p>Comparison of grain diameter distribution for grains emitted during the abrasion test. APV values for mortar sample M3—reference (blue) vs. TiO<sub>2</sub>-modified samples (red) for grain diameters of 0.523 ÷ 19.810 μm.</p>
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<p>SEM micrograph of a grain of agglomerated TiO<sub>2</sub> nanocrystallites mobilized from cementitious mortar (M1)—confirmation of chemical composition presented through an EDS analysis; the entire agglomerate had a diameter of approx. 1.50 µm.</p>
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<p>SEM micrograph of mobilized grains through an abrasion test of the mortar’s surface (M2) and immobilized on the adhesive fiber, with magnification on the immobilized material.</p>
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<p>EDS analysis for different mobilized grains presented in an SEM micrograph in <a href="#materials-17-03022-f011" class="html-fig">Figure 11</a>; all EDS signals indicate a mix of various compounds at the exact location (red marker)—grains consisting of hydration products with TiO<sub>2</sub> grains embedded within.</p>
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<p>SEM micrograph of mobilized grains through an abrasion test of the mortar’s surface (M3) and immobilized on the adhesive fiber, with magnification on the immobilized material.</p>
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<p>EDS analysis for different mobilized grains presented in an SEM micrograph in <a href="#materials-17-03022-f013" class="html-fig">Figure 13</a>; all EDS signals indicate a mix of different compounds at the exact location (red marker)—grains consisting of hydration products with TiO<sub>2</sub> grains embedded within.</p>
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12 pages, 4726 KiB  
Article
Experimental Investigation of Damping Properties of Selected Polymer Materials
by Lucjan Witek and Piotr Łabuński
Materials 2024, 17(12), 3021; https://doi.org/10.3390/ma17123021 - 20 Jun 2024
Cited by 1 | Viewed by 796
Abstract
This paper presents the results of an experimental modal analysis of a beam covered by polymer materials used as a passive vibration isolation. The main aim of this study was to determine the damping properties of selected viscoelastic materials. In order to check [...] Read more.
This paper presents the results of an experimental modal analysis of a beam covered by polymer materials used as a passive vibration isolation. The main aim of this study was to determine the damping properties of selected viscoelastic materials. In order to check the damping properties of tested materials, an experimental modal analysis, with the use of an electrodynamic vibration system, was performed. In this study, four kinds of specimens were considered. In the first step of the work, the beam made out of aluminum alloy was investigated. Afterwards, a cantilever beam was covered with a layer of bitumen-based material acting as a damper. This method is commonly known as a free layer damping treatment (FLD). In order to increase the damping capabilities, the previous configuration was improved by fixing a thin aluminum layer directly to the viscoelastic core. Such a treatment is called constrained layer damping (CLD). Subsequently, another polymer (butyl rubber) in the CLD configuration was tested for its damping properties. As a result of the performed experimental modal analysis, the frequencies of resonant vibrations and their corresponding amplitudes were obtained. The experimental results were used to quantitatively evaluate the damping properties of tested materials. Full article
(This article belongs to the Section Mechanics of Materials)
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<p>Loss factor, η, and storage modulus, E, as a function of frequency [<a href="#B6-materials-17-03021" class="html-bibr">6</a>,<a href="#B7-materials-17-03021" class="html-bibr">7</a>].</p>
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<p>Viscoelastic materials damping: (<b>a</b>) FLD treatment and (<b>b</b>) CLD treatment [<a href="#B6-materials-17-03021" class="html-bibr">6</a>,<a href="#B7-materials-17-03021" class="html-bibr">7</a>].</p>
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<p>View of investigated beam fixed to the head of the shaker in CLD treatment.</p>
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<p>Location of piezoelectric acceleration sensors used in modal analysis (sensor no. 1 defined in control channel; and sensor no. 2—measure channel).</p>
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<p>Specimens used in experimental investigations.</p>
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<p>Frequency response curves for specimen numbers 1, 2 and 3.</p>
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<p>Frequency response curves for specimens: no. 2 (FLD treatment) and no. 3 (CLD treatment).</p>
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<p>Frequency response curves for specimens nos. 1, 3 and 4.</p>
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<p>Frequency response curves for specimen nos. 3 and 4.</p>
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<p>Relative amplitude of acceleration, <math display="inline"><semantics> <mrow> <mrow> <mrow> <msubsup> <mrow> <mi>A</mi> </mrow> <mrow> <mn>2</mn> </mrow> <mrow> <mi>i</mi> </mrow> </msubsup> </mrow> <mo>/</mo> <mrow> <msubsup> <mrow> <mi>A</mi> </mrow> <mrow> <mn>2</mn> </mrow> <mrow> <mn>1</mn> </mrow> </msubsup> </mrow> </mrow> </mrow> </semantics></math>, of specimens nos. 2, 3 and 4 for all resonant frequencies.</p>
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<p>Relative amplitude of acceleration, <math display="inline"><semantics> <mrow> <mrow> <mrow> <msubsup> <mrow> <mi>A</mi> </mrow> <mrow> <mn>2</mn> </mrow> <mrow> <mi>i</mi> </mrow> </msubsup> </mrow> <mo>/</mo> <mrow> <msubsup> <mrow> <mi>A</mi> </mrow> <mrow> <mn>2</mn> </mrow> <mrow> <mn>1</mn> </mrow> </msubsup> </mrow> </mrow> </mrow> </semantics></math>, of specimens nos. 2, 3 and 4 for resonant frequencies range of 79.8–2578 Hz.</p>
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20 pages, 13744 KiB  
Article
Research on Alloying Elements’ Influence on CuETP-Grade Copper’s Mechanical and Electrical Properties
by Krystian Franczak, Michał Sadzikowski, Paweł Kwaśniewski, Grzegorz Kiesiewicz, Wojciech Ściężor and Szymon Kordaszewski
Materials 2024, 17(12), 3020; https://doi.org/10.3390/ma17123020 - 20 Jun 2024
Viewed by 990
Abstract
The continuous industrial development that occurs worldwide generates the need to develop new materials with increasingly higher functional properties. This need also applies to the basic material for electricity purposes, which is copper. In this article, we carry out studies on the influence [...] Read more.
The continuous industrial development that occurs worldwide generates the need to develop new materials with increasingly higher functional properties. This need also applies to the basic material for electricity purposes, which is copper. In this article, we carry out studies on the influence of various alloying elements such as Mg, In, Si, Nb, Hf, Sb, Ni, Al, Fe, Zr, Cr, Zn, P, Ag, Sc, Pb, Sn, Co, Ti, Mn, Te and Bi on the electrical and mechanical properties of ETP-grade copper. The research involves producing copper alloys using the gravity die casting method with alloy additions of 0.1 wt.%, 0.3 wt.% and 0.5 wt.%. All resulting materials are cold-worked to produce wires, which are subsequently homogenized and annealed. The materials produced in this manner undergo testing to determine their specific electrical conductivity, tensile strength, yield strength, elongation and Vickers hardness (HV10 scale). Full article
(This article belongs to the Special Issue Characterization, Properties, and Applications of New Metallic Alloys)
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<p>(<b>a</b>) Increase in copper electrical resistivity as a function of different impurities’ concentration [<a href="#B13-materials-17-03020" class="html-bibr">13</a>]; (<b>b</b>) Influence of various impurities on electrical conductivity (approximated results) [<a href="#B4-materials-17-03020" class="html-bibr">4</a>].</p>
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<p>Comparison of mechanical and electrical properties of various copper alloys [<a href="#B1-materials-17-03020" class="html-bibr">1</a>,<a href="#B6-materials-17-03020" class="html-bibr">6</a>,<a href="#B27-materials-17-03020" class="html-bibr">27</a>].</p>
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<p>Schematic representation of research program.</p>
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<p>Influence of Mg on copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of In on copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Si on copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Nb on copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Hf on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Sb on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Ni on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Al on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Fe on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Zr on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Cr on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Zn on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of P on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Ag on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Sc on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Pb on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Sn on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Co on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Ti on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Mn on CuETP copper UTS, YS, elongation (diagram on the <b>left</b>), hardness and electrical conductivity (diagram on the <b>right</b>).</p>
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<p>Influence of Te on CuETP copper hardness and electrical conductivity.</p>
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<p>Influence of Bi on CuETP copper hardness and electrical conductivity.</p>
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<p>Electrical conductivity as a function of alloying elements’ content in CuETP copper—annealed temper.</p>
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<p>Ultimate tensile strength as a function of alloying elements’ content in CuETP copper—annealed temper.</p>
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<p>Yield strength as a function of alloying elements’ content in CuETP copper—annealed temper.</p>
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<p>Elongation as a function of alloying elements’ content in CuETP copper—annealed temper.</p>
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<p>Hardness as a function of alloying elements’ content in CuETP copper—annealed temper.</p>
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11 pages, 6782 KiB  
Article
Effect of the Height of a 3D-Printed Model on the Force Transmission and Thickness of Thermoformed Orthodontic Aligners
by Omar Ghoraba, Christoph Bourauel, Mostafa Aldesoki, Lamia Singer, Ahmed M. Ismail, Hanaa Elattar, Abdulaziz Alhotan and Tarek M. Elshazly
Materials 2024, 17(12), 3019; https://doi.org/10.3390/ma17123019 - 20 Jun 2024
Viewed by 1266
Abstract
This research aims to investigate the influence of model height employed in the deep drawing of orthodontic aligner sheets on force transmission and aligner thickness. Forty aligner sheets (Zendura FLX) were thermoformed over four models of varying heights (15, 20, 25, and 30 [...] Read more.
This research aims to investigate the influence of model height employed in the deep drawing of orthodontic aligner sheets on force transmission and aligner thickness. Forty aligner sheets (Zendura FLX) were thermoformed over four models of varying heights (15, 20, 25, and 30 mm). Normal contact force generated on the facial surface of the upper right central incisor (Tooth 11) was measured using pressure-sensitive films. Aligner thickness around Tooth 11 was measured at five points. A digital caliper and a micro-computed tomography (µ-CT) were employed for thickness measurements. The normal contact force exhibited an uneven distribution across the facial surface of Tooth 11. Model 15 displayed the highest force (88.9 ± 23.2 N), while Model 30 exhibited the lowest (45.7 ± 15.8 N). The force distribution was more favorable for bodily movement with Model 15. Thickness measurements revealed substantial thinning of the aligner after thermoforming. This thinning was most pronounced at the incisal edge (50% of the original thickness) and least at the gingivo-facial part (85%). Additionally, there was a progressive reduction in aligner thickness with increasing model height, which was most significant on the facial tooth surfaces. We conclude that the thermoplastic aligner sheets undergo substantial thinning during the thermoforming process, which becomes more pronounced as the height of the model increases. As a result, there is a decrease in both overall and localized force transmission, which could lead to increased tipping by the aligner and a diminished ability to achieve bodily movement. Full article
(This article belongs to the Special Issue Orthodontic Materials: Properties and Effectiveness of Use)
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<p>Different 3D-printed aligned resin models used for thermoforming, exhibiting varying heights. A shallow groove was positioned 2 mm beyond the gingival line to facilitate the standardization of aligner trimming.</p>
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<p>A visual representation of the procedure followed for measuring the local normal contact force, generated on the crown of a maxillary right central incisor (Tooth 11), using Fuji<sup>®</sup> pressure-sensitive film. The pressurized film underwent scanning with a scanner, and the 2D scan was superimposed over a 3D digital model of the tooth to enhance visualization.</p>
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<p>A µ-CT processed 3D image for a part of the aligner over the upper right central incisor (Tooth 11) for measurement of aligner thickness by MIMICS 25.0 software, at various reference points (gingivo-facial (GF), mid-facial (MF), incisal (I), mid-lingual (ML), gingivo-lingual (GL)).</p>
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<p>Normal contact force generated on Tooth 11 by aligners, made from Zendura FLX sheets thermoformed over models of different heights (15, 20, 25, 30 mm), and recorded using Fuji pressure-sensitive film. Different uppercase and lowercase superscript letters indicate a statistically significant difference within the same horizontal row and vertical column, respectively.</p>
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<p>Thickness of aligners, made from Zendura FLX sheets thermoformed over models of different heights (15, 20, 25, 30 mm), recorded using a digital caliper at different points of the aligner splint covering the crown of Tooth 11. Different lowercase superscript letters indicate a statistically significant difference within the same vertical column.</p>
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<p>Thickness of aligners, made from Zendura FLX sheets thermoformed over models of different heights (15, 20, 25, 30 mm), recorded using a µ-CT device at different points of the aligner splint covering the crown of Tooth 11. Different lowercase superscript letters indicate a statistically significant difference within the same vertical column.</p>
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17 pages, 5067 KiB  
Article
Unloading Model of Elastic–Plastic Half-Space Contacted by an Elastic Spherical Indenter
by Wenhao Xie, Yuanyuan Guo, Huaiping Ding, Xiaochun Yin and Panpan Weng
Materials 2024, 17(12), 3018; https://doi.org/10.3390/ma17123018 - 20 Jun 2024
Viewed by 1001
Abstract
A new unloading contact model of an elastic–perfectly plastic half-space indented by an elastic spherical indenter is presented analytically. The recovered deformation of the elastic indenter and the indented half-space has been found to be dependent on the elastic modulus ratio after fully [...] Read more.
A new unloading contact model of an elastic–perfectly plastic half-space indented by an elastic spherical indenter is presented analytically. The recovered deformation of the elastic indenter and the indented half-space has been found to be dependent on the elastic modulus ratio after fully unloading. The recovered deformation of the indented half-space can be calculated based on the deformation of the purely elastic indenter. The unloading process is assumed to be entirely elastic, and then the relationship of contact force and indentation can be determined based on the solved recovered deformation and conforms to Hertzian-type. The model can accurately predict the residual indentation and residual curvature radius after fully unloading. Numerical simulations are performed to demonstrate the assumptions and the unloading model. The proposed unloading model can cover a wide range of indentations and material properties and is compared with existing unloading models. The cyclic behavior including loading and unloading can be predicted by combining the proposed unloading law with the existing contact loading model. The combined model can be employed for low-velocity impact and nanoindentation tests and the comparison results are in good agreement. Full article
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<p>Schematic of elastic contact between half-space and sphere.</p>
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<p>Loading and unloading contact between elastic–plastic half-space and elastic sphere.</p>
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<p>The mesh of the fundamental FE model: (<b>a</b>) contact region, (<b>b</b>) overall view of the mesh.</p>
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<p>Comparison of FE results with Hertzian theory: (<b>a</b>) contact force, (<b>b</b>) contact radius.</p>
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<p>Validations of Hertzian unloading law: (<b>a</b>) material case (1), (<b>b</b>) material case (2).</p>
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<p>Error of the residual indentation <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>δ</mi> </mrow> <mrow> <mi>r</mi> </mrow> </msub> </mrow> </semantics></math>.</p>
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<p>Comparison of residual curvature radius between Equation (25) and FE fitting: (<b>a</b>) material case (2), (<b>b</b>) material case (3), (<b>c</b>) material case (4), (<b>d</b>) material case (5).</p>
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<p>Comparisons of the unloading laws and FE results for different maximum indentations with material case (2): (<b>a</b>) 5.2<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>δ</mi> </mrow> <mrow> <mi>Y</mi> </mrow> </msub> </mrow> </semantics></math> (<b>b</b>) 83.4<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>δ</mi> </mrow> <mrow> <mi>Y</mi> </mrow> </msub> </mrow> </semantics></math>, (<b>c</b>) 683.4<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>δ</mi> </mrow> <mrow> <mi>Y</mi> </mrow> </msub> </mrow> </semantics></math>, (<b>d</b>) 6346.9<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>δ</mi> </mrow> <mrow> <mi>Y</mi> </mrow> </msub> </mrow> </semantics></math>.</p>
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<p>Comparisons of the unloading laws and FE results for different maximum indentations with the material of case (3): (<b>a</b>) small indentations, (<b>b</b>) large indentations.</p>
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<p>Comparisons of unloading models and the FE result with different maximum indentations for material case (3): (<b>a</b>) <math display="inline"><semantics> <mrow> <mn>13.5</mn> <msub> <mrow> <mi>δ</mi> </mrow> <mrow> <mi>Y</mi> </mrow> </msub> <mo>,</mo> <mi>a</mi> <mo>/</mo> <msup> <mrow> <mi>R</mi> </mrow> <mrow> <mo>∗</mo> </mrow> </msup> <mo>=</mo> <mn>0.03</mn> </mrow> </semantics></math>, (<b>b</b>) <math display="inline"><semantics> <mrow> <mn>105.1</mn> <msub> <mrow> <mi>δ</mi> </mrow> <mrow> <mi>Y</mi> </mrow> </msub> <mo>,</mo> <mi>a</mi> <mo>/</mo> <msup> <mrow> <mi>R</mi> </mrow> <mrow> <mo>∗</mo> </mrow> </msup> <mo>=</mo> <mn>0.1</mn> </mrow> </semantics></math>, (<b>c</b>) <math display="inline"><semantics> <mrow> <mn>843.1</mn> <msub> <mrow> <mi>δ</mi> </mrow> <mrow> <mi>Y</mi> </mrow> </msub> <mo>,</mo> <mi>a</mi> <mo>/</mo> <msup> <mrow> <mi>R</mi> </mrow> <mrow> <mo>∗</mo> </mrow> </msup> <mo>=</mo> <mn>0.4</mn> </mrow> </semantics></math>.</p>
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<p>Comparison of present combined contact model and FE results: (<b>a</b>) material case (2), (<b>b</b>) material case (3), (<b>c</b>) material case (4), (<b>d</b>) material case (5).</p>
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<p>Comparison of present combined contact model and impact simulations: (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>v</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> <mo>=</mo> <mn>5</mn> </mrow> </semantics></math> m/s, impact (3), (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>v</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> <mo>=</mo> <mn>3</mn> </mrow> </semantics></math> m/s, impact (4), (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>v</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> <mo>=</mo> <mn>5</mn> </mrow> </semantics></math> m/s, impact (5), (<b>d</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>v</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> <mo>=</mo> <mn>3</mn> </mrow> </semantics></math> m/s, impact (6).</p>
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<p>Comparisons of the indentation test results and present combined models.</p>
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13 pages, 9385 KiB  
Article
Yttria-Stabilized Zirconia Composite Coating as Barrier to Reduce Hydrogen Permeation into Steel
by Jianmeng Wu, Jiaqi Xie, Mengyuan He, Jingyi Zhang and Songjie Li
Materials 2024, 17(12), 3017; https://doi.org/10.3390/ma17123017 - 20 Jun 2024
Viewed by 1062
Abstract
Hydrogen atoms can enter into metallic materials through penetration and diffusion, leading to the degradation of the mechanical properties of the materials, and the application of hydrogen barrier coatings is an effective means to alleviate this problem. Zirconia coatings (ZrO2) have [...] Read more.
Hydrogen atoms can enter into metallic materials through penetration and diffusion, leading to the degradation of the mechanical properties of the materials, and the application of hydrogen barrier coatings is an effective means to alleviate this problem. Zirconia coatings (ZrO2) have been widely studied as a common hydrogen barrier coating, but zirconia undergoes a crystalline transition with temperature change, which can lead to volumetric changes in the coating and thus cause problems such as cracking and peeling of the coating. In this work, ZrO2 coating was prepared on a Q235 matrix using a sol-gel method, while yttria-stabilized zirconia (YSZ) coatings with different contents of rare earth elements were prepared in order to alleviate a series of problems caused by the crystal form transformation of ZrO2. The coating performances were evaluated by the electrochemical hydrogen penetration test, pencil hardness test, scratch test, and high-temperature oxidation test. The results show that yttrium can improve the stability of the high-temperature phase of ZrO2, alleviating the cracking problem of the coating due to the volume change triggered by the crystalline transition; improve the consistency of the coating; and refine the grain size of the oxide. The performance of YSZ coating was strongly influenced by the yttria doping mass, and the coating with 10 wt% yttria doping had the best hydrogen barrier performance, the best antioxidant performance, and the largest adhesion. Compared with the matrix, the steady-state hydrogen current density of the YSZ coating decreased by 72.3%, the antioxidant performance was improved by 65.8%, and the ZrO2 coating hardness and adhesion levels were B and 4B, respectively, while YSZ coating hardness and adhesion were upgraded to 2H and 5B. With the further increase in yttrium doping mass, the hardness of the coating continued to improve, but the defects of the coating increased, resulting in a decrease in the hydrogen barrier performance, antioxidant performance, and adhesion. In this work, the various performances of ZrO2 coating were significantly improved by doping with the rare earth element, which provides a reference for further development and application of oxide coatings. Full article
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<p>Schematic diagram of electrochemical hydrogen penetration test device.</p>
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<p>TG (<b>a</b>), DTG (<b>b</b>), and DSC (<b>c</b>) curves of ZrO<sub>2</sub> and YSZ sol.</p>
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<p>SEM images of (<b>a</b>) ZrO<sub>2</sub> coating, (<b>b</b>) 5YSZ, (<b>c</b>) 10YSZ and (<b>d</b>) 15YSZ coatings surface.</p>
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<p>Element distribution on the surface of YSZ coating: (<b>a</b>) morphology, (<b>b</b>) Zr element distribution, (<b>c</b>) O element distribution, (<b>d</b>) Y element distribution.</p>
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<p>XRD patterns of ZrO<sub>2</sub> and YSZ coating.</p>
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<p>Pencil hardness statistics of ZrO<sub>2</sub> coating and YSZ coating.</p>
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<p>Topography of the (<b>a</b>) ZrO<sub>2</sub> coating, (<b>b</b>) 5YSZ, (<b>c</b>) 10YSZ and (<b>d</b>) 15YSZ coating after scratch test. (Note: The dashed circles in the figure represent the locations where the coating was peeling off).</p>
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<p>Graph of antioxidant property test results of samples: (<b>a</b>) weight gain as a function of time, (<b>b</b>) weight gain squared as a function of time.</p>
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<p>(<b>a</b>) Electrochemical hydrogen permeation curves and corresponding (<b>b</b>) hydrogen permeation flux curves of the matrix and coatings.</p>
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17 pages, 5108 KiB  
Article
Investigation on Anti-Fuel Erosion Performance of Sasobit/SBS-Modified Asphalt and Its Mixtures
by Yongkang Wu, Meizhu Chen, Qi Jiang, Jianwei Zhang, Yansong Fan and Jun He
Materials 2024, 17(12), 3016; https://doi.org/10.3390/ma17123016 - 19 Jun 2024
Viewed by 697
Abstract
The fuel leakage of fuel vehicles will exacerbate the occurrence of distresses on asphalt pavements, including peeling, chipping and potholes, especially under the synergistic effect of traffic load and environment. In this research, Sasobit, which is commonly used as a warm agent in [...] Read more.
The fuel leakage of fuel vehicles will exacerbate the occurrence of distresses on asphalt pavements, including peeling, chipping and potholes, especially under the synergistic effect of traffic load and environment. In this research, Sasobit, which is commonly used as a warm agent in asphalt, is selected as the anti-fuel erosion agent and incorporated into SBS-modified asphalt and its mixtures. Diesel and gasoline are selected as the fuel erosion media. Sasobit/SBS-modified asphalt binder and its mixtures are investigated for fuel erosion. The rheological properties of bitumen and the mechanical properties of asphalt mixtures are assessed. The experimental findings show that the dissolution velocity of SBS-modified asphalt with 3% Sasobit is 0.2%/min for diesel erosion, while it is 1.7%/min for gasoline erosion, lower than the control sample without Sasobit. Meanwhile, the rutting factor of Sasobit/SBS-modified asphalt decreases less than that of the control sample without Sasobit. Furthermore, the mass loss ratio after the Cantabro test of Sasobit/SBS-modified asphalt mixtures is 1.2% for diesel erosion, while it is 6.8% for gasoline erosion, lower than that of the control sample without Sasobit. The results of the mechanical properties for asphalt mixtures demonstrate that Sasobit can enhance the anti-fuel erosion performance. Moreover, the research results of the Sasobit modification mechanism show that Sasobit can form a microcrystalline structure in SBS-modified asphalt, which subsequently improves the anti-fuel of asphalt and its mixtures. This research provides a reference for anti-fuel erosion assessment methods and solutions to improve the anti-fuel erosion of asphalt pavement. Full article
(This article belongs to the Section Construction and Building Materials)
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<p>Fuel pollution of asphalt pavements: (<b>a</b>) fuel film of asphalt pavement, (<b>b</b>) fuel leakage due to vehicle breakdown and (<b>c</b>) fuel leakage due to traffic accidents.</p>
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<p>The experimental flow chart of this research.</p>
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<p>Aggregate gradation for AC-13 asphalt mixtures.</p>
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<p>Fuel immersion experiment device of asphalt.</p>
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<p>Fuel immersion experiment device of asphalt mixtures.</p>
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<p>The influence of Sasobit on the <span class="html-italic">R<sub>m</sub></span> of the SBS-modified asphalt immersed in diesel or gasoline.</p>
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<p>Influence of diesel and gasoline on the rutting factor of SBS-modified asphalt.</p>
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<p>The influence of Sasobit on the rutting factor of SBS-modified asphalt immersed in fuel: (<b>a</b>) diesel; (<b>b</b>) gasoline.</p>
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<p>FT-IR spectra of Sasobit, SBS-modified asphalt and Sasobit/SBS-modified asphalt.</p>
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<p>Fluorescence microscopic images of different asphalts: (<b>a</b>) SBS-modified asphalt; (<b>b</b>) Sasobit/SBS-modified asphalt.</p>
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<p>The appearance of the samples after the fuel immersion test.</p>
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<p>Mass loss ratios of SBS-modified asphalt mixtures with different fuel immersion times: (<b>a</b>) diesel immersion; (<b>b</b>) gasoline immersion.</p>
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<p>The influence of Sasobit on the Δ<span class="html-italic">m</span><sub>2</sub> of SBS-modified asphalt mixtures.</p>
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<p>The influence of Sasobit on the <span class="html-italic">MS</span> of SBS-modified asphalt mixtures.</p>
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<p>The influence of Sasobit on the <span class="html-italic">MS</span><sub>0</sub> of the SBS-modified asphalt mixtures.</p>
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<p>Influence of Sasobit on the <span class="html-italic">R<sub>T</sub></span> of SBS-modified asphalt mixtures.</p>
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<p>Correlations of different anti-fuel erosion tests results.</p>
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11 pages, 4733 KiB  
Article
Synthesis and Characterization of Sol–Gelled Barium Zirconate as Novel MTA Radiopacifiers
by Hsiu-Na Lin, May-Show Chen, Pei-Jung Chang, Yao-Chi Lee, Chin-Yi Chen, Yuh-Jing Chiou and Chung-Kwei Lin
Materials 2024, 17(12), 3015; https://doi.org/10.3390/ma17123015 - 19 Jun 2024
Viewed by 783
Abstract
Barium zirconate (BaZrO3, BZO), which exhibits superior mechanical, thermal, and chemical stability, has been widely used in many applications. In dentistry, BZO is used as a radiopacifier in mineral trioxide aggregates (MTAs) for endodontic filling applications. In the present study, BZO [...] Read more.
Barium zirconate (BaZrO3, BZO), which exhibits superior mechanical, thermal, and chemical stability, has been widely used in many applications. In dentistry, BZO is used as a radiopacifier in mineral trioxide aggregates (MTAs) for endodontic filling applications. In the present study, BZO was prepared using the sol–gel process, followed by calcination at 700–1000 °C. The calcined BZO powders were investigated using X-ray diffraction and scanning electron microscopy. Thereafter, MTA-like cements with the addition of calcined BZO powder were evaluated to determine the optimal composition based on radiopacity, diametral tensile strength (DTS), and setting times. The experimental results showed that calcined BZO exhibited a majority BZO phase with minor zirconia crystals. The crystallinity, the percentage, and the average crystalline size of BZO increased with the increasing calcination temperature. The optimal MTA-like cement was obtained by adding 20% of the 700 °C-calcined BZO powder. The initial and final setting times were 25 and 32 min, respectively. They were significantly shorter than those (70 and 56 min, respectively) prepared with commercial BZO powder. It exhibited a radiopacity of 3.60 ± 0.22 mmAl and a DTS of 3.02 ± 0.18 MPa. After 28 days of simulated oral environment storage, the radiopacity and DTS decreased to 3.36 ± 0.53 mmAl and 2.84 ± 0.27 MPa, respectively. This suggests that 700 °C-calcined BZO powder has potential as a novel radiopacifier for MTAs. Full article
(This article belongs to the Special Issue New Materials and Techniques for Root Canal Preparation and Filling)
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<p>(<b>a</b>) XRD pattern and (<b>b</b>) SEM photo of commercial barium zirconate (C-BZO) powder.</p>
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<p>Radiopacity of MTA-like cements prepared by adding 20, 30, and 40% of commercial BZO powder. The red dashed line indicates the ISO standard requirement (3 mmAl).</p>
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<p>Diametral tensile strength of MTA-like cements prepared by adding 20, 30, and 40% of commercial BZO powder.</p>
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<p>Thermogravimetric analysis (TGA), derivative thermogravimetry (DTG), and differential scanning calorimetry (DSC) curves for as-prepared sol–gelled BZO powder.</p>
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<p>XRD patterns of sol–gelled BZO powders after calcination at 700, 800, 900, and 1000 °C for 2 h. The sol–gelled and 700–1000 °C-calcined BZO powders were coded as BZO-7, -8, -9, and -10, respectively.</p>
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<p>(<b>a</b>) Percentage of composition and (<b>b</b>) average crystalline size of sol–gelled BZO powders calcined at 700, 800, 900, and 1000 °C for 2 h.</p>
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<p>SEM images of sol–gelled barium titanate calcined at (<b>a</b>) 700, (<b>b</b>) 800, (<b>c</b>) 900, and (<b>d</b>) 1000 °C for 2 h.</p>
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<p>Histogram analysis of grain sizes from SEM images for sol–gelled barium titanate calcined at (<b>a</b>) 700, (<b>b</b>) 800, (<b>c</b>) 900, and (<b>d</b>) 1000 °C for 2 h.</p>
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<p>Radiopacity of MTA-like cements prepared by adding 20% of various BZO powders. The red dashed line indicates the ISO standard requirement (3 mmAl).</p>
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<p>DTS of MTA-like cements prepared by adding 20% of various BZO powders.</p>
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<p>Initial and final setting times for selected MTA-like cements prepared by adding 20% of various BZO powders and solidified with powder/water = 3:1. Pure Portland cement (PC) was also used for comparison.</p>
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