[go: up one dir, main page]
More Web Proxy on the site http://driver.im/
You seem to have javascript disabled. Please note that many of the page functionalities won't work as expected without javascript enabled.
 
 
Sign in to use this feature.

Years

Between: -

Subjects

remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline

Journals

remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline

Article Types

Countries / Regions

remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline

Search Results (8,082)

Search Parameters:
Keywords = rolling

Order results
Result details
Results per page
Select all
Export citation of selected articles as:
23 pages, 1136 KiB  
Article
A Reasoned Attempt to Mitigate Vibrations in Nonlinear Flexible Systems Influenced by Tractive–Elastic Rolling Contact Friction Through Input Shaping: A Case Study on a Trolley–Pipe Benchmark Transport System
by Gerardo Peláez, Pablo Izquierdo, Gustavo Peláez and Higinio Rubio
Actuators 2025, 14(2), 97; https://doi.org/10.3390/act14020097 (registering DOI) - 17 Feb 2025
Abstract
The well-regarded feedforward control strategy known as Input Shaping is aimed at improving the dynamic response of flexible mechanical systems by reducing overshoot and residual vibration amplitude. Its validity has been confirmed by numerous studies dealing with linear system dynamics. However, its application [...] Read more.
The well-regarded feedforward control strategy known as Input Shaping is aimed at improving the dynamic response of flexible mechanical systems by reducing overshoot and residual vibration amplitude. Its validity has been confirmed by numerous studies dealing with linear system dynamics. However, its application in nonlinear systems, particularly those influenced by tractive–elastic rolling contact friction, remains a challenging and less explored open research area. This paper investigates whether Input Shaping, without tractive rolling friction compensation, can effectively mitigate vibrations in a trolley–pipe benchmark transport system. In this system, the pipe is modeled as a rolling disc attached to the trolley by a spring at its center of mass, while the trolley itself is connected to a guiding body frame by an additional spring acting as a proportional control. The natural frequencies of the system are analytically estimated and numerically verified from a corresponding well-suited multibody model. Thus, tailored two-mode shapers are designed based on simultaneous constraints and the convolution sum, respectively. Through multibody simulations, this study evaluates the performance of Input Shaping under tractive–elastic rolling contact friction conditions. The findings highlight both the potential and limitations of this control method in addressing nonlinear mechanical systems influenced by tractive–elastic rolling contact friction. Full article
(This article belongs to the Special Issue Nonlinear Active Vibration Control)
Show Figures

Figure 1

Figure 1
<p>Application Unshaped and ZV-filtered responses to a step input: The unshaped input and its corresponding response are shown on the left, while the shaped input and the resulting vibration-suppressed response appear on the right.</p>
Full article ">Figure 2
<p>(<b>a</b>) Physical representation of the mass-spring-damper system under gross-sliding friction force. (<b>b</b>) Block diagram representation of the system dynamics by the Laplace model.</p>
Full article ">Figure 3
<p>Response of the mass-spring system under gross-slip friction, without the derivative damper action, to a nonzero initial position. Conditions: <math display="inline"><semantics> <mrow> <mi>k</mi> <mo>=</mo> <mn>5</mn> </mrow> </semantics></math> [N/m], <math display="inline"><semantics> <mrow> <mi>m</mi> <mo>=</mo> <mn>0.20</mn> </mrow> </semantics></math> [Kg], <math display="inline"><semantics> <mrow> <mi>μ</mi> <mo>=</mo> <mn>0.15</mn> </mrow> </semantics></math>.</p>
Full article ">Figure 4
<p>Elastic rolling contact of a cylinder rolling freely on a plane under normal load P.</p>
Full article ">Figure 5
<p>(<b>a</b>) Reference model of a two-mass and spring system undergoing rolling friction. (<b>b</b>) Impulse response of the rolling disc, showing the nearly undamped x-position of the mass center.</p>
Full article ">Figure 6
<p>Steel coil transport system in manufacturing plants.</p>
Full article ">Figure 7
<p>The Multibody System is broken up into the spring element ① and the super-element ②.</p>
Full article ">Figure 8
<p>Simscape Mechanical Explorer Sketch of the system showing the body frames.</p>
Full article ">Figure 9
<p>Simscape (Matlab) multibody model of the system showing bodies interconnected by kinematics joints plus a large number of important multibody formalisms by rigid frame transforms plus body and joint customizations.</p>
Full article ">Figure 10
<p>FFT of the signal corresponding to the abscissa position of the center of mass of the pipe. Low-frequency component value 0.079998 [Hz]. High-frequency component 0.159997 [Hz].</p>
Full article ">Figure 11
<p>Convolved two-mode ZVD-ZVD shaper for <math display="inline"><semantics> <mrow> <msub> <mi>f</mi> <mn>1</mn> </msub> </mrow> </semantics></math>: 0.07998 and <math display="inline"><semantics> <mrow> <msub> <mi>f</mi> <mn>2</mn> </msub> </mrow> </semantics></math>: 0.159997 Hz undamped frequencies.</p>
Full article ">Figure 12
<p>Two-mode input shaper by simultaneous constraints for <math display="inline"><semantics> <mrow> <msub> <mi>f</mi> <mn>1</mn> </msub> </mrow> </semantics></math>: 0.07998 and <math display="inline"><semantics> <mrow> <msub> <mi>f</mi> <mn>2</mn> </msub> </mrow> </semantics></math>: 0.159997 [Hz] and <math display="inline"><semantics> <mrow> <mi>ζ</mi> </mrow> </semantics></math>: 0.0.</p>
Full article ">Figure 13
<p>Trapezoidal input motion. Conditions: the ramp-up lasts for <math display="inline"><semantics> <mrow> <mi>t</mi> <msub> <mi>t</mi> <mn>1</mn> </msub> </mrow> </semantics></math>: 17 [s]. Unshaped input motion. Direct–ZVD-ZVD shaped input motion. Conditions: ramp-up lasts for <math display="inline"><semantics> <mrow> <mi>t</mi> <msub> <mi>t</mi> <mn>1</mn> </msub> <mo>+</mo> <msub> <mi>T</mi> <mn>5</mn> </msub> </mrow> </semantics></math>: 33 [s].</p>
Full article ">Figure 14
<p>Multibody model pipe mass center X-position responses to trapezoidal input motion profile with 12 s ramp-up. Pipe mass center X-position unshaped response. Pipe mass center X-position shaped response for direct–ZVD-ZVD shaped input motion.</p>
Full article ">Figure 15
<p>Trapezoidal input motion. Conditions: the ramp-up lasts for <math display="inline"><semantics> <mrow> <mi>t</mi> <msub> <mi>t</mi> <mn>1</mn> </msub> </mrow> </semantics></math>: 20 [s]. Unshaped input motion. Convolved–ZVD-ZVD shaped input motion.</p>
Full article ">Figure 16
<p>Experimental trapezoidal input motion profile responses. Pipe mass center X-position unshaped response. Pipe mass center X-position for convolved–ZVD-ZVD shaped response.</p>
Full article ">
18 pages, 3816 KiB  
Article
Experimental Investigation and FEM Simulation of the Tensile Behavior of Hot-Rolled Quenching and Partitioning 5Mn Steel
by Firew Tullu Kassaye, Tamiru Hailu Kori, Aleksandra Kozłowska and Adam Grajcar
Materials 2025, 18(4), 868; https://doi.org/10.3390/ma18040868 (registering DOI) - 17 Feb 2025
Viewed by 22
Abstract
Medium manganese steels provide a good combination of tensile strength and ductility due to their multiphase microstructure produced during the multi-step heat treatment process. This study primarily focused on testing and analyzing the tensile properties of 0.17C-5Mn-0.76Al-0.9Si-Nb medium manganese quenching and partitioning (QP) [...] Read more.
Medium manganese steels provide a good combination of tensile strength and ductility due to their multiphase microstructure produced during the multi-step heat treatment process. This study primarily focused on testing and analyzing the tensile properties of 0.17C-5Mn-0.76Al-0.9Si-Nb medium manganese quenching and partitioning (QP) steel using both the experimental and finite element method (FEM) in the multilinear isotropic hardening material model. The 7 mm and 12 mm thick plates exhibited a similar microstructure of tempered primary martensite, lath-type retained austenite, and secondary martensite. The experiments measured tensile strengths of 1400 MPa for 12 mm round specimens and 1325 MPa for 7 mm flat specimens, with total elongations of 15% for round specimens and 11% for flat specimens. The results indicated that the sample’s geometry has some effect on the UTS and ductility of the studied medium-Mn QP steel. However, the more important is the complex relationship between the plate thickness and yield stress and ductility, which are affected by finishing hot rolling conditions. The FEM results showed that the von Mises stresses for flat and round specimens were 1496 MPa and 1514 MPa, respectively, and were consistent with the calculated true stresses of experimental results. This shows that numerical modeling, specifically a multilinear isotropic hardening material model, properly describes the material properties beyond the yield stress and accurately predicts the plastic deformation of the investigated multiphase QP steel. Full article
(This article belongs to the Section Metals and Alloys)
Show Figures

Figure 1

Figure 1
<p>Processing schedule of investigated steel (FRT—finishing rolling temperature).</p>
Full article ">Figure 2
<p>Tensile test specimen dimensions: (<b>a</b>) round specimen from 12 mm thickness plate; (<b>b</b>) flat specimen from 7 mm thickness plate.</p>
Full article ">Figure 2 Cont.
<p>Tensile test specimen dimensions: (<b>a</b>) round specimen from 12 mm thickness plate; (<b>b</b>) flat specimen from 7 mm thickness plate.</p>
Full article ">Figure 3
<p>Meshing: (<b>a</b>) round specimen; (<b>b</b>) flat specimen; boundary condition: (<b>c</b>) flat specimen; (<b>d</b>) round specimen: the round specimen from 12 mm thickness plate; the flat specimen from 7 mm thickness plate.</p>
Full article ">Figure 4
<p>SEM micrographs after quenching at 240 °C and partitioning at 450 °C (300 s): (<b>a</b>) plate 7 mm; (<b>b</b>) plate 12 mm. PM—primary martensite; SM—secondary martensite; RA—retained austenite.</p>
Full article ">Figure 5
<p>Comparison of averaged engineering and true stress-strain curves of investigated Q240P450(300 s) steel: (<b>a</b>) 12 mm thickness round specimen; (<b>b</b>) 7 mm thickness flat specimen.</p>
Full article ">Figure 6
<p>Strain hardening rate curves as a function of true strain for both plate thickness.</p>
Full article ">Figure 7
<p>FEM simulation results of equivalent (von-Mises) stresses for Q240P450(300 s): (<b>a</b>) flat specimen; (<b>b</b>) round specimen.</p>
Full article ">Figure 8
<p>Comparison of experimental and FEM stress-strain curves: (<b>a</b>) Q240P450(300 s)—12 mm plate thickness; (<b>b</b>) Q240P450(300 s)—7 mm plate thickness.</p>
Full article ">
26 pages, 6004 KiB  
Article
Design and Control Strategies of Multirotors with Horizontal Thrust-Vectored Propellers
by Ricardo Rosales Martinez, Hannibal Paul and Kazuhiro Shimonomura
Drones 2025, 9(2), 145; https://doi.org/10.3390/drones9020145 - 16 Feb 2025
Viewed by 101
Abstract
With the growing adoption of Unmanned Aerial Vehicles (UAVs) in industrial and commercial sectors, the limitations of traditional under-actuated multirotors are becoming increasingly evident, particularly in manipulation tasks. Limited control over the thrust vector direction of the propellers, coupled with its interdependence on [...] Read more.
With the growing adoption of Unmanned Aerial Vehicles (UAVs) in industrial and commercial sectors, the limitations of traditional under-actuated multirotors are becoming increasingly evident, particularly in manipulation tasks. Limited control over the thrust vector direction of the propellers, coupled with its interdependence on the vehicle’s roll, pitch, and yaw moments, significantly restricts manipulation capabilities. To address these challenges, this work presents a control framework for multirotor UAVs equipped with thrust-vectoring components, enabling enhanced control over the direction of lateral forces. The framework supports various actuator configurations by integrating fixed vertical propellers with horizontally mounted thrust-vectoring components. It is capable of handling horizontal thruster setups that generate forces in all directions along the x- and y-axes. Alternatively, it accommodates constrained configurations where the vehicle is limited to generating force in a single direction along either the x- or y-axis. The supported UAVs can follow transmitter commands, setpoints, or predefined trajectories, while the flight controller autonomously manages the propellers and thrusters to achieve the desired motion. Moment evaluations were conducted to assess the torsional capabilities of the vehicles by varying the angles of the thrusters during torsional tasks. The results demonstrate comparable torsional magnitudes to previously studied thrust-vectoring UAVs. Simulations with vehicles of varying inertia and dimensions showed that, even with large horizontal thruster offsets, the vehicles followed desired trajectories while maintaining stable horizontal orientation and smaller attitude variations compared to normal flight. Similar performance was observed with positive and negative vertical offsets, demonstrating the framework’s tolerance for thrusters outside the horizontal plane. Full article
(This article belongs to the Special Issue Dynamics Modeling and Conceptual Design of UAVs)
17 pages, 5708 KiB  
Article
Boosting the Optical Activity of Titanium Oxide Through Conversion from Nanoplates to Nanotubes and Nanoparticle-Supported Nanolayers
by Adil Alshoaibi
Crystals 2025, 15(2), 187; https://doi.org/10.3390/cryst15020187 - 16 Feb 2025
Viewed by 204
Abstract
The nano-architecture of titanium oxide is a key element of a wide range of applications, mainly optical and catalytic activities. Therefore, the current study focuses on engineering and designing three interesting nanostructures of titanium oxides: nanoplates, nanotubes, and nanoparticle-supported nanolayers. The nanoplates of [...] Read more.
The nano-architecture of titanium oxide is a key element of a wide range of applications, mainly optical and catalytic activities. Therefore, the current study focuses on engineering and designing three interesting nanostructures of titanium oxides: nanoplates, nanotubes, and nanoparticle-supported nanolayers. The nanoplates of titanium oxides were prepared and confirmed by TEM images, X-ray diffraction, and EDX analysis. These nanoplates have an anatase phase, with the distance across the corners in the range of 15 nm. These nanoplates were modified and developed through a rolling process with sodium doping to generate the Na-doped TiO2 nanotubes. These nanotubes were observed by TEM images and X-ray diffraction. In addition, the doping process of titanium oxides with sodium was confirmed by EDX analysis. A novel nano-architecture of titanium oxide was designed by supporting titanium oxide nanoparticles over Zn/Al nanolayers. The optical properties and activity of titanium oxides with the different morphologies indicated that titanium oxides became a highly photo-active photocatalyst after conversion to nanotubes. This finding was observed through the reduction in the band gap energy to 2.7 eV. Additionally, after 37 min of exposure to UV light, the titanium oxide nanotubes totally broke down and transformed the green dye of NGB into carbon dioxide and water. Furthermore, the kinetic analysis verified that the green dyes’ degradation was expedited by the high activity of nanotubes. Ultimately, based on these findings, it was possible to design an efficient photocatalyst for water purification by converting nanoplates into nanotubes, doping titanium sites with sodium ions, and creating new active sites for titanium oxides through defect-induced super radical formation. Full article
(This article belongs to the Special Issue Synthesis and Characterization of Oxide Nanoparticles)
Show Figures

Figure 1

Figure 1
<p>Titanium oxide TNP-450: (<b>a</b>) TEM, (<b>b</b>) TEM after magnification, and (<b>c</b>) EDX.</p>
Full article ">Figure 2
<p>X-ray diffraction of TNP after thermal treatment: (<b>a</b>) 450 °C and (<b>b</b>) 100 °C.</p>
Full article ">Figure 3
<p>Titanium oxide TNTS: (<b>a</b>) TEM, (<b>b</b>) EDX and (<b>c</b>) XRD.</p>
Full article ">Figure 4
<p>SEM images of TNSN: (<b>a</b>) at 100 nm and (<b>b</b>) after magnification.</p>
Full article ">Figure 5
<p>X-ray diffraction of TNSN at: (<b>a</b>) 450 °C, (<b>b</b>) 200 °C, and (<b>c</b>) room temperature.</p>
Full article ">Figure 6
<p>Absorbance spectra of (<b>a</b>) TNP-450 and (<b>b</b>) TNTS-450.</p>
Full article ">Figure 7
<p>Band gap energy of (<b>a</b>) TNP-450 and (<b>b</b>) TNTS-450.</p>
Full article ">Figure 8
<p>Absorbance spectra of TNSN: (<b>a</b>) room temperature, (<b>b</b>) 200 °C, and (<b>c</b>) 450 °C.</p>
Full article ">Figure 9
<p>Band gap energy of TNSN: (<b>a</b>) room temperature, (<b>b</b>) 200 °C, and (<b>c</b>) 450 °C.</p>
Full article ">Figure 10
<p>Absorbance spectra of NGB with different irradiation times in UV light in the presence of the prepared TiO<sub>2</sub>-nanoplates (TNP-450).</p>
Full article ">Figure 11
<p>Absorbance spectra of NGB with different irradiation times in UV light in the presence of the prepared TiO<sub>2</sub>-nanotubes (TNTS-450).</p>
Full article ">Figure 12
<p>Absorbance spectra of NGB with different irradiation times in UV light in the presence of: (<b>a</b>) the nanoparticles TiO<sub>2</sub>-supported nanolayers after thermal treatment at 450 °C (TNSN-450) and (<b>b</b>) the commercial TiO<sub>2</sub>.</p>
Full article ">Figure 13
<p>Kinetic studies obtained for the photocatalytic degradation of the green dyes in the UV light using: (<b>a</b>) nanotubes (TNTS-450), (<b>b</b>) nanoplates (TNP-450), (<b>c</b>) nanoparticle-supported nanolayers (TNSN-450), and (<b>d</b>) the commercial TiO<sub>2</sub>.</p>
Full article ">
18 pages, 6370 KiB  
Review
Anatomy-Based Filler Injection: Treatment Techniques for Supraorbital Hollowness and Charming Roll
by Gi-Woong Hong, Wonseok Choi, Jovian Wan, Song Eun Yoon, Carlos Bautzer, Lucas Basmage, Patricia Leite and Kyu-Ho Yi
Life 2025, 15(2), 304; https://doi.org/10.3390/life15020304 - 15 Feb 2025
Viewed by 223
Abstract
Supraorbital hollowness and pretarsal fullness, commonly known as the sunken eyelid and charming roll, respectively, are significant anatomical features that impact the aesthetic appearance of the periorbital region. Supraorbital hollowness is characterized by a recessed appearance of the upper eyelid, often attributed to [...] Read more.
Supraorbital hollowness and pretarsal fullness, commonly known as the sunken eyelid and charming roll, respectively, are significant anatomical features that impact the aesthetic appearance of the periorbital region. Supraorbital hollowness is characterized by a recessed appearance of the upper eyelid, often attributed to genetic factors, aging, or surgical alterations, such as excessive fat removal during blepharoplasty. This condition is particularly prevalent among East Asians due to anatomical differences, such as weaker levator muscles and unique fat distribution patterns. Pretarsal fullness, also known as aegyo-sal, enhances the youthful and expressive appearance of the lower eyelid, forming a roll above the lash line that is considered aesthetically desirable in East Asian culture. Anatomical-based filler injection techniques are critical for correcting these features, involving precise placement within the correct tissue planes to avoid complications and achieve natural-looking results. This approach not only improves the aesthetic appeal of the eyelid but also enhances the overall facial harmony, emphasizing the importance of tailored procedures based on individual anatomy and cultural preferences. Full article
Show Figures

Figure 1

Figure 1
<p>Before (<b>A</b>) and after (<b>B</b>) treatment of supraorbital hollowness.</p>
Full article ">Figure 2
<p>Anatomical layers of the supraorbital region.</p>
Full article ">Figure 3
<p>Vascular structures of the orbital region.</p>
Full article ">Figure 4
<p>Injection entry point and technique for the cannula. Injection entry point: Vertical line drawn above or outside the lateral canthus, around the lower margin of the superior orbital rim. Focus on the medial and middle parts of the periorbital rim, under the brow, to avoid the supraorbital and supratrochlear main arteries. Above the supratarsal lid crease and below the orbicularis retaining ligament. Injection technique: Patient in vertical sitting position with voluntarily opened eyes. Retrograde linear tiny injection technique with very slow release.</p>
Full article ">Figure 5
<p>Anatomy of the preseptal space.</p>
Full article ">Figure 6
<p>Injection planes: Supraperiosteal and submuscular injections around the orbital rim over the orbital septum to fill the hollowness. Subdermal injection of very soft HA filler to smooth the surface and remove unnecessary multiple eyelid lines.</p>
Full article ">Figure 7
<p>Ideal position and shape of the eyebrow.</p>
Full article ">Figure 8
<p>Ratio difference between the size of the eye and eyebrow.</p>
Full article ">Figure 9
<p>Common classification of eyebrow shapes around the world.</p>
Full article ">Figure 10
<p>Retro-orbicularis oculi fat (ROOF) in the eyebrow region.</p>
Full article ">Figure 11
<p>Injection plane for the cannula. Submuscular injection into ROOF (retro-orbicularis oculi fat) for eyebrow augmentation. Subdermal injection of very soft filler to even out the surface and remove unnecessary multiple eyelid lines.</p>
Full article ">Figure 12
<p>Structure of the lower eyelid roll muscle.</p>
Full article ">Figure 13
<p>Injection techniques for the cannula or needle. Linear threading, retrograde tiny injection, very slow release, serial puncture, and tenting technique.</p>
Full article ">Figure 14
<p>Injection planes: Deep subdermal or supramuscular injections. Subdermal injection to smooth the surface, close to the eyelash.</p>
Full article ">Figure 15
<p>Anatomy of the superior and inferior palpebral arteries.</p>
Full article ">
28 pages, 6329 KiB  
Article
Analytical and Experimental Research of Lubrication Load-Bearing Characteristics of Microtextured Meshing Interface
by Xigui Wang, Jiafu Ruan, Yongmei Wang and Weiqiang Zou
Materials 2025, 18(4), 845; https://doi.org/10.3390/ma18040845 (registering DOI) - 14 Feb 2025
Viewed by 208
Abstract
The excellent lubrication and load-bearing synergistic modulation of the meshing interface has been well recognized, as the microtextured tooth surface seems to be a punished area in deep-sea gear thermal elastohydrodynamic lubrication (TEHL). This is mainly because of the traditional perception of the [...] Read more.
The excellent lubrication and load-bearing synergistic modulation of the meshing interface has been well recognized, as the microtextured tooth surface seems to be a punished area in deep-sea gear thermal elastohydrodynamic lubrication (TEHL). This is mainly because of the traditional perception of the anti-scuffing load-bearing capacity (ASLBC) and the similarity of the interfacial microelement configurations. Microtextured contact can be applied to the meshing interface to adjust the time-varying TEHL characteristics and enhance the meshing load-bearing performance. In this study, the analytical homogeneous equivalent micro-hydrodynamic contact multiscale parameters are determined, and the dispersed micro-flow real distribution area of the texturing interface is indicated, revealing the TEHL friction characteristics of the rolling–sliding line contact microelement, which is regarded as a bridge connecting the micro-dynamic pressure discrete contact friction behavior and the TEHL textured interface meshed-gear load-bearing. The contact model mentioned theoretically predicts the evolutionary time-varying characteristics of the micro-thermoelastic lubrication behavior of the textured contact interface under hydrodynamic conditions and demonstrates that the microtextured configuration parameters of the molecular scale meshing interface are the most influential structural parameters for the load-bearing problem of the homogeneous flow pressure film layer between the gear pair tooth surfaces, especially for deep-sea gear meshing load-bearing reliability under limited lubrication space. Full article
Show Figures

Figure 1

Figure 1
<p>Organizational framework for the content of this study.</p>
Full article ">Figure 2
<p>Technical lines of research for this thesis.</p>
Full article ">Figure 3
<p>Discrete and continuous textures microelements.</p>
Full article ">Figure 4
<p>Multiscale characterization of textured microelement interfaces (homogeneous arrangement density and geometrical configuration parameters).</p>
Full article ">Figure 5
<p>An equivalent homogenization of microelementary textured interfacial parts in resolved domains.</p>
Full article ">Figure 6
<p>An algorithm flow chart of the texture multiscale microelementary lubrication model accounting for ASLBC capacity enhancement.</p>
Full article ">Figure 7
<p>Illustration of microtextured gear pair meshing simulation: (<b>a</b>) analysis process flowchart; (<b>b</b>) MIMT model and MTME morphology scale distribution density.</p>
Full article ">Figure 8
<p>Biological microprocessing removal mechanism of Acidithiobacillus ferrooxidans.</p>
Full article ">Figure 9
<p>Microfabrication MTME experimental procedure for Thiobacillus ferrooxidans.</p>
Full article ">Figure 10
<p>Model and object of experimental platforms for biomicrofabricated MTMEs: (<b>a</b>) experimental platform model; (<b>b</b>) experimental platform object.</p>
Full article ">Figure 11
<p>Friction behavior and wear properties of textured microelement interfaces test rig: (<b>a</b>) MFT-5000-RETC testing machine; (<b>b</b>) specimen fixture; (<b>c</b>) textured microelement sample.</p>
Full article ">Figure 12
<p>Solution model for coverage ratio of MTME interface in microprocessing.</p>
Full article ">Figure 13
<p>Detailed description of the thermoelastic dynamic contact simulation experiments: (<b>a</b>) simulation test rig for line contact of pin-block disk; (<b>b</b>) experimental validation of simulation analysis; (<b>c</b>) test rig for actual texturing of meshing interface contacts; (<b>d</b>) TEHL dynamic pressure interface temperature measurement; (<b>e</b>) preparation of microtextured samples by biological microfabrication removal method.</p>
Full article ">Figure 13 Cont.
<p>Detailed description of the thermoelastic dynamic contact simulation experiments: (<b>a</b>) simulation test rig for line contact of pin-block disk; (<b>b</b>) experimental validation of simulation analysis; (<b>c</b>) test rig for actual texturing of meshing interface contacts; (<b>d</b>) TEHL dynamic pressure interface temperature measurement; (<b>e</b>) preparation of microtextured samples by biological microfabrication removal method.</p>
Full article ">Figure 14
<p>Time-varying characteristics of contact friction at interfaces with different textured m-croelements: (<b>a</b>) friction coefficient curves of textured interfaces; (<b>b</b>) friction coefficient curves of smooth interfaces without microelements at different linear velocities.</p>
Full article ">Figure 15
<p>Lubrication and load-bearing properties of the textured interface in different MTME configurations: (<b>a</b>) time-varying load-bearing capacity of textured interface versus MTME depth; (<b>b</b>) time-varying contact friction coefficient of the textured interface versus MTME depth.</p>
Full article ">Figure 16
<p>Textured microelement lubrication interface load-bearing test bench: (<b>a</b>) layout sketch; (<b>b</b>) three-dimensional drawing; (<b>c</b>) type platform; (<b>d</b>) experimental gear unit.</p>
Full article ">Figure 16 Cont.
<p>Textured microelement lubrication interface load-bearing test bench: (<b>a</b>) layout sketch; (<b>b</b>) three-dimensional drawing; (<b>c</b>) type platform; (<b>d</b>) experimental gear unit.</p>
Full article ">Figure 17
<p>Characterization of textured interface meshing loads at different distribution densities.</p>
Full article ">Figure 18
<p>Time-varying curves of output torque for meshing loads.</p>
Full article ">Figure 19
<p>Time-varying curves of output torque variance for meshed loads.</p>
Full article ">Figure 20
<p>The morphological characteristics of meshing interface anti-scuffing failures of different microelement configurations: (<b>a</b>) changing law of friction coefficient and meshing load-bearing of circular pits microtextured interface; (<b>b</b>) changing law of friction coefficient and meshing load-bearing of square pits microtextured interface; (<b>c</b>) ASLBC and contact strength factor for microtextured and non-microtextured meshing interfaces.</p>
Full article ">Figure 21
<p>Time-varying of TEHL minimum homogeneous layer film thickness for the multiscale textured interface of micro-concave pit.</p>
Full article ">Figure 22
<p>Time-varying laws of meshing interface homogeneous microelement contact pressure with different sliding line speeds. (<b>a</b>) Load applied set to 0.2 kN (with MIMT); (<b>b</b>) Load applied set to 0.5 kN (with MIMT); (<b>c</b>) Load applied set to 0.2 kN (without MIMT); (<b>d</b>) Load applied set to 0.5 kN (without MIMT).</p>
Full article ">
16 pages, 16681 KiB  
Article
Achieving Strength–Ductility Balance in TWIP Steel by Tailoring Cementite
by Zhenyu Zhao, Jian Sheng, Dazhao Li, Shaobin Bai, Yongan Chen, Haitao Lu, Pengfei Cao and Xin Liu
Materials 2025, 18(4), 843; https://doi.org/10.3390/ma18040843 (registering DOI) - 14 Feb 2025
Viewed by 240
Abstract
High-Mn steels are widely used in various fields. However, the FCC structure is not conducive to improving strength, limiting their development and application. In this work, hot-rolled Fe-25Mn-1Al-3Si-1C (wt.%) steel was annealed at various temperatures to tailor the cementite particles and recrystallized grains, [...] Read more.
High-Mn steels are widely used in various fields. However, the FCC structure is not conducive to improving strength, limiting their development and application. In this work, hot-rolled Fe-25Mn-1Al-3Si-1C (wt.%) steel was annealed at various temperatures to tailor the cementite particles and recrystallized grains, thus achieving a balance between strength and ductility. As the annealing temperature increased from 550 to 650 °C, the volume fraction of recrystallized grains slightly increased and the volume fraction of cementite particles initially increased and then decreased, which was explained and verified by the quantitative calculation. Especially, the high-density pre-dislocation and finely dispersed cementite particles in sample AN550 resulted in a relatively low volume fraction of recrystallized grains. Interestingly, secondary deformation twinning was activated during the subsequent tensile deformation in addition to the dislocations, stacking faults, and previous deformation twinning. This complex interaction among various deformation mechanisms indued a good balance between strength and ductility, achieving an outstanding result (58.9 GPa%) regarding tensile strength and total elongation. This work offers an effective route for developing a high-Mn TWIP steel with outstanding strength–ductility balance. Full article
(This article belongs to the Special Issue From Materials to Applications: High-Performance Steel Structures)
Show Figures

Figure 1

Figure 1
<p>Abstract process flow diagram.</p>
Full article ">Figure 2
<p>SEM microstructures of samples: (<b>a</b>) HR; (<b>b</b>) AN550; (<b>c</b>) AN600; (<b>d</b>) AN650. (<b>e</b>) EDS result of cementite particles in sample AN600. (<b>f</b>) XRD spectra of samples under various conditions.</p>
Full article ">Figure 3
<p>EBSD and TEM micrographs of samples under various conditions. (<b>a</b>–<b>d</b>) The phase diagrams of coexisting austenite and precipitate: HR, AN550, AN600 and AN650, respectively. (<b>e</b>) shows the precipitates observed in the AN550 sample, and (<b>f</b>) is the EDS map of the red region of (<b>e</b>).</p>
Full article ">Figure 4
<p>(<b>a</b>,<b>b</b>) are the volume fraction and average grain size of the carbides, respectively.</p>
Full article ">Figure 5
<p>KAM maps of the samples under various conditions. (<b>a</b>) HR, (<b>b</b>) AN550, (<b>c</b>) AN600, (<b>d</b>) AN650. 0–1°, recrystallized grains; 1–5°, non-recrystallized grains.</p>
Full article ">Figure 6
<p>(<b>a</b>) KAM distribution map of the sample. (<b>b</b>) Average grain size distribution of the sample under various conditions (excluding Mn segregation band).</p>
Full article ">Figure 7
<p>Mechanical responses at different annealing temperatures. (<b>a</b>) Engineering stress–strain curves; (<b>b</b>) the tensile mechanical properties of samples in terms of yield strength, ultimate tensile strength, total elongation, and UTS × TE.</p>
Full article ">Figure 8
<p>The contribution of the individual strengthening mechanism and the experimental yield strength.</p>
Full article ">Figure 9
<p>Recrystallized distribution maps of samples AN550 (<b>a</b>), AN600 (<b>b</b>), and AN650 (<b>c</b>), respectively. The red, yellow, and blue colors represented the deformed, partially recrystallized, and fully recrystallized grains, respectively.</p>
Full article ">Figure 10
<p>Work hardening rate (WHR) and fracture morphologies of annealed samples: (<b>a</b>) sample HR; (<b>b</b>) sample AN550; (<b>c</b>) sample AN600; (<b>d</b>) sample AN650.</p>
Full article ">Figure 11
<p>The interrupted tensile microstructures of sample AN550 under various true strains. (<b>a</b>) Before deformation. (<b>b</b>,<b>c</b>) At a true strain of 0.15, (<b>b</b>) dislocation tangles and dislocation walls; (<b>c</b>) stacking faults and twins near GB. (<b>d</b>–<b>f</b>) At a true strain of 0.3, (<b>d</b>) twin and L-C lock; (<b>e</b>,<b>f</b>) are the bright and dark field images, respectively. (<b>g</b>–<b>i</b>) After fracture, (<b>g</b>,<b>h</b>) are the bright field and HRTEM images of the initial and secondary twins, respectively; (<b>i</b>) is an inverse fast Fourier transform (IFFT) image.</p>
Full article ">Figure 12
<p>TEM images of sample AN650. (<b>a</b>) represents the microstructure prior to deformation, which displays a recrystallized structure; (<b>b</b>,<b>c</b>) are the microstructures after fracture; (<b>b</b>) shows the interaction between M<sub>3</sub>C and dislocations; (<b>c</b>) shows primary twins and secondary twins.</p>
Full article ">Figure 13
<p>Microstructural evolution diagrams of different samples after annealing (<b>a</b>–<b>d</b>), and after deformation for AN550 and AN650 samples (<b>e</b>,<b>f</b>). (<b>a</b>) HR; (<b>b</b>,<b>e</b>) AN550; (<b>c</b>) AN600; (<b>d</b>,<b>f</b>) AN650.</p>
Full article ">
21 pages, 1848 KiB  
Article
Two-Step Optimization Method of Freight Train Speed Curve Based on Rolling Optimization Algorithm and MPC
by Xubin Sun, Jingjing Li, Wei Zhang, Guiyang Sun, Xiyao Zhang and Hongze Xu
Vehicles 2025, 7(1), 17; https://doi.org/10.3390/vehicles7010017 - 14 Feb 2025
Viewed by 202
Abstract
Given the considerable length and weight of freight trains, their operation can be quite challenging. Improper operation may lead to train decoupling and derailment. Driver Advisory Systems (DASs) are used in some countries to assist train drivers by providing the speed curves, which [...] Read more.
Given the considerable length and weight of freight trains, their operation can be quite challenging. Improper operation may lead to train decoupling and derailment. Driver Advisory Systems (DASs) are used in some countries to assist train drivers by providing the speed curves, which are desired to be easy to track. Multi-mass train model is a good choice to depict the in-train forces in train speed curve generating, but its application is often hindered by the computation time. A single mass train model is considered as another choice to simplify the computation. To exploit the advantages of the multi-mass and single-mass models, this paper proposes a Two-step Optimization Method to generate the optimal speed curves for the freight trains. In the first step, the Rolling Optimization Algorithm (ROA) is proposed to optimize the speed curve on the basis of the single-mass model, taking the train energy consumption and punctuality as the optimization objectives. In order to assist the driver in operating the train smoothly, the speed curve generated by the ROA was tested on DAS, but it could not be followed accurately in the actual operation. To solve this problem, a Model Predictive Control (MPC) algorithm based on a multi-mass model is adopted as the second optimization step, which takes the output speed curve of the ROA as the reference speed curve. The MPC algorithm will generate a new speed curve, taking in-train forces, energy consumption and punctuality as the optimization indices. Simulations are carried out using the data from the Dalailong railway in China to evaluate the proposed method. The simulation results show that the speed curves generated by the Two-step Optimization Method are smoother than that of the ROA, and the throttle sequences are more conducive for the driver to follow in practical operation. The simulation results show that the energy consumption is reduced by 17.1% compared to that of the ROA simulation. The speed curve also can be integrated into the onboard DAS or the Automatic Train Operation (ATO) system, aiming to obtain a smooth and energy-efficient train operation. Full article
Show Figures

Figure 1

Figure 1
<p>Two-step optimization method framework.</p>
Full article ">Figure 2
<p>Comparison of the original and the equivalent gradient.</p>
Full article ">Figure 3
<p>Slope type demonstration.</p>
Full article ">Figure 4
<p>Flowchart of Rolling Optimization Algorithm for freight train speed curve.</p>
Full article ">Figure 5
<p>Comparison of the traction switching points for the uphill section.</p>
Full article ">Figure 6
<p>Comparison of the coast switching points for the downhill section.</p>
Full article ">Figure 7
<p>Speed curves connecting method.</p>
Full article ">Figure 8
<p>MPC algorithm demonstration.</p>
Full article ">Figure 9
<p>Train multi-mass model.</p>
Full article ">Figure 10
<p>Force analysis for a single locomotive/wagon.</p>
Full article ">Figure 11
<p>Coupler force with different <math display="inline"><semantics> <msub> <mi>k</mi> <mi>d</mi> </msub> </semantics></math> when <math display="inline"><semantics> <msub> <mi>k</mi> <mi>a</mi> </msub> </semantics></math> = 0.1, <math display="inline"><semantics> <msub> <mi>k</mi> <mi>b</mi> </msub> </semantics></math> = 10.</p>
Full article ">Figure 12
<p>Coupler force with different <math display="inline"><semantics> <msub> <mi>k</mi> <mi>d</mi> </msub> </semantics></math> when <math display="inline"><semantics> <msub> <mi>k</mi> <mi>a</mi> </msub> </semantics></math> = 0.01, <math display="inline"><semantics> <msub> <mi>k</mi> <mi>b</mi> </msub> </semantics></math> = 10.</p>
Full article ">Figure 13
<p>Simulation speed curves with different weighting coefficients.</p>
Full article ">Figure 14
<p>Partially enlarged simulation speed curves with different weighting coefficients.</p>
Full article ">Figure 15
<p>Coupler force with different <math display="inline"><semantics> <msub> <mi>N</mi> <mi>p</mi> </msub> </semantics></math> and <math display="inline"><semantics> <msub> <mi>N</mi> <mi>c</mi> </msub> </semantics></math>.</p>
Full article ">Figure 16
<p>Simulation speed curves with different <math display="inline"><semantics> <msub> <mi>N</mi> <mi>p</mi> </msub> </semantics></math> and <math display="inline"><semantics> <msub> <mi>N</mi> <mi>c</mi> </msub> </semantics></math>.</p>
Full article ">Figure 17
<p>Partially enlarged simulation speed curves with different <math display="inline"><semantics> <msub> <mi>N</mi> <mi>p</mi> </msub> </semantics></math> and <math display="inline"><semantics> <msub> <mi>N</mi> <mi>c</mi> </msub> </semantics></math>.</p>
Full article ">Figure 18
<p>Train speed curves and coupler force comparisons.</p>
Full article ">Figure 19
<p>Control strategy comparison chart.</p>
Full article ">
20 pages, 10631 KiB  
Article
Improving Low-Frequency Vibration Energy Harvesting of a Piezoelectric Cantilever with Quasi-Zero Stiffness Structure: Theory and Experiment
by Chunli Hua, Donglin Zou and Guohua Cao
Actuators 2025, 14(2), 93; https://doi.org/10.3390/act14020093 - 14 Feb 2025
Viewed by 224
Abstract
In this study, a novel cantilever piezoelectric energy harvester is constructed by using a quasi-zero stiffness (QZS) structure. The QZS structure consists of a classic piezoelectric cantilever beam combined with some accessories that include two pre-compression springs, rolling bearings, slideways and a cylindrical [...] Read more.
In this study, a novel cantilever piezoelectric energy harvester is constructed by using a quasi-zero stiffness (QZS) structure. The QZS structure consists of a classic piezoelectric cantilever beam combined with some accessories that include two pre-compression springs, rolling bearings, slideways and a cylindrical cam. The purpose of the QZS structure is to reduce the natural frequencies of the harvester, so that it can more efficiently collect low-frequency vibration energy. In this study, firstly, the extended Hamilton variational principle is used to establish the dynamic equations of the continuous system. Secondly, the Galerkin method is used to discretize the partial differential equation, and then the analytical solutions of the output voltage, current, power and vibration response of the harvester are obtained. Finally, the influence of the QZS structure on energy harvesting characteristics is studied. Theoretical research shows that the QZS structure can effectively reduce the fundamental natural frequency of the cantilever beam and improve its energy harvesting efficiency. When the spring stiffness is about half of the bending stiffness of the cantilever beam, the uncoupled fundamental natural frequency of the harvester is quasi-zero. For the experimental device considered here, experiments show that the QZS structure can reduce the fundamental natural frequency from 76.4 Hz to 54.1 Hz, decreasing by 22.3 Hz. The maximum output power is increased from 1.43 mW/g2 to 1.95 mW/g2, an increase of 36.4%. The experimental results validate the theoretical model. In short, this paper provides a new idea for the design of energy harvesters suitable for low-frequency vibration. Full article
(This article belongs to the Section Actuator Materials)
Show Figures

Figure 1

Figure 1
<p>A cantilevered piezoelectric energy harvester with QZS (bimorph configuration, series or parallel connection): (<b>a</b>) isometric view; (<b>b</b>) side view.</p>
Full article ">Figure 2
<p>Schematic diagram of installation deviation of the rolling bearing.</p>
Full article ">Figure 3
<p>Comparisons of (<b>a</b>) mode shapes and (<b>b</b>) natural frequencies.</p>
Full article ">Figure 4
<p>Comparisons of fundamental natural frequency with different (<b>a</b>) stiffness ratio and (<b>b</b>) mass ratio.</p>
Full article ">Figure 5
<p>Results comparisons between present calculation and study by Erturk [<a href="#B38-actuators-14-00093" class="html-bibr">38</a>]: (<b>a</b>) voltage FRF; (<b>b</b>) current FRF; (<b>c</b>) power FRF; (<b>d</b>) tip velocity FRF.</p>
Full article ">Figure 6
<p>The (<b>a</b>) first natural frequencies, (<b>b</b>) second natural frequencies and (<b>c</b>) third natural frequencies under different compression ratios.</p>
Full article ">Figure 7
<p>The (<b>a</b>) first natural frequencies, (<b>b</b>) second natural frequencies and (<b>c</b>) third natural frequencies under different stiffness ratios.</p>
Full article ">Figure 8
<p>Electromechanical FRFs for different stiffnesses of horizontal spring: (<b>a</b>) voltage FRF; (<b>b</b>) power FRF; (<b>c</b>) tip acceleration FRF.</p>
Full article ">Figure 9
<p>The sensitivity analysis of <span class="html-italic">x</span><sub>0</sub>/<span class="html-italic">d</span>: (<b>a</b>) voltage FRF; (<b>b</b>) power FRF; (<b>c</b>) tip acceleration FRF.</p>
Full article ">Figure 10
<p>The designed energy harvester: (<b>a</b>) design model; (<b>b</b>) physical model; (<b>c</b>) partial enlargement of the physical model.</p>
Full article ">Figure 11
<p>Experimental setup used for validation of the analytical model.</p>
Full article ">Figure 12
<p>(<b>a</b>) Input time−domain acceleration; (<b>b</b>) power spectrum of input acceleration; (<b>c</b>) voltage output FRF; (<b>d</b>) coherence functions.</p>
Full article ">Figure 13
<p>Comparison of theoretical and experimental FRFs: (<b>a</b>) tip displacement FRF; (<b>b</b>) voltage FRF; (<b>c</b>) power FRF.</p>
Full article ">
9 pages, 5868 KiB  
Article
A Novel Method to Determine Deformation Strain in a High-Temperature Mushy Zone for a Typical Electrical Strip Under Twin-Roll Strip Casting
by Wenli Hu, Yali Hou, Jianhui Shi, Jinhua Zhao and Lifeng Ma
Crystals 2025, 15(2), 178; https://doi.org/10.3390/cryst15020178 - 13 Feb 2025
Viewed by 260
Abstract
An evaluation method was proposed to calculate the deformation strain of a high-temperature mushy zone (HTMZ) related to twin-roll strip casting (TSC) with regard to typical 6.5 wt.% Si electrical steel (6.5 Si steel) on the basis of the crystal—plasticity theory. The viscoplasticity [...] Read more.
An evaluation method was proposed to calculate the deformation strain of a high-temperature mushy zone (HTMZ) related to twin-roll strip casting (TSC) with regard to typical 6.5 wt.% Si electrical steel (6.5 Si steel) on the basis of the crystal—plasticity theory. The viscoplasticity self-consistent (VPSC) model was applied to calculate the evolution discipline of crystallographic orientation (CRO) for the studied 6.5 Si steel processed by different deformation strains under a deformation mode of plane strain, and the deformation strain of HTMZ for the studied 6.5 Si steel related to TSC was further estimated by comparing the CRO feature achieved by theoretical calculation and experimental characterization. Results indicate that the distribution feature of CRO obtained by theoretical calculation becomes increasingly similar to those obtained through experimental characterization with the deformation strains increasing from 0 to 1.5. The ratio between the distribution intensities corresponding to R-Cube texture, the typical rolling texture of α-fiber, and the Cube texture achieved by theoretical calculation is the closest to the value obtained by experimental characterization at deformation strain of 1.4, and the deformation strain of HTMZ for the studied 6.5 Si steel involved in TSC is determined to be ~1.4. Full article
(This article belongs to the Section Crystalline Metals and Alloys)
Show Figures

Figure 1

Figure 1
<p>Crystallographic information of studied alloy obtained through EBSD analysis. (<b>a</b>) Three-dimensional morphology of grains. (<b>b</b>) Distribution of grain size corresponding to different sections for the 6.5 Si steel processed by TSC.</p>
Full article ">Figure 2
<p>Constructed initial CRO for 6.5 Si steel before TSC treatment expressed by utilizing a pole figure. (<b>a</b>) (100) pole figure. (<b>b</b>) (110) pole figure. (<b>c</b>) (111) pole figure.</p>
Full article ">Figure 3
<p>Crystallographic orientation feature of the investigated 6.5 Si steel. (<b>a</b>) Orientation and grain boundary distribution graph. (<b>b</b>) ODF (phi2 = 45°).</p>
Full article ">Figure 4
<p>Orientation evolution of {001} crystallographic orientation. (<b>a</b>) 0; (<b>b</b>) 0.3; (<b>c</b>) 0.7; (<b>d</b>) 1.1; (<b>e</b>) 1.5. (<b>f</b>) Variation trends of texture features.</p>
Full article ">Figure 5
<p>The calculated results associated with the deformation mechanism of the studied alloy. (<b>a</b>) Average number of active systems. (<b>b</b>) Relative activity induced by different slip systems considering the multiple slip system of <math display="inline"><semantics> <mrow> <mfenced open="{" close="" separators="|"> <mrow> <mfenced open="" close="}" separators="|"> <mrow> <mn>110</mn> </mrow> </mfenced> <mo>&lt;</mo> <mn>111</mn> <mo>&gt;</mo> <mo>,</mo> <mfenced open="{" close="" separators="|"> <mrow> <mfenced open="" close="}" separators="|"> <mrow> <mn>112</mn> </mrow> </mfenced> <mo>&lt;</mo> <mn>111</mn> <mo>&gt;</mo> </mrow> </mfenced> </mrow> </mfenced> <mo>,</mo> <mfenced open="{" close="" separators="|"> <mrow> <mfenced open="" close="}" separators="|"> <mrow> <mn>123</mn> </mrow> </mfenced> <mo>&lt;</mo> <mn>111</mn> <mo>&gt;</mo> </mrow> </mfenced> </mrow> </semantics></math>.</p>
Full article ">
22 pages, 3145 KiB  
Article
Improvement in Performance Characteristics of Bitumen and Bituminous Mixtures by Means of Polyvinyl Acetate
by Yalçın Oğuz Hetemoğlu, Mustafa Kürşat Çubuk and Metin Gürü
Constr. Mater. 2025, 5(1), 9; https://doi.org/10.3390/constrmater5010009 - 13 Feb 2025
Viewed by 228
Abstract
This paper examines the improvement in the performance characteristics and the rheological properties of modified bitumen through the addition of the thermoplastic polymer polyvinyl acetate (PVA). PVA is a synthetic polymer derived from the polymerization of the vinyl acetate. The effect of PVA [...] Read more.
This paper examines the improvement in the performance characteristics and the rheological properties of modified bitumen through the addition of the thermoplastic polymer polyvinyl acetate (PVA). PVA is a synthetic polymer derived from the polymerization of the vinyl acetate. The effect of PVA on bitumen and bituminous mixtures was investigated through the conventional (penetration, softening point, force-ductility, elastic recovery, Marshall and Nicholson stripping tests) and Superpave (rotational viscosity (RV), rolling thin film oven (RTFOT), pressure aging vessel (PAV), dynamic shear rheometer (DSR) and beam bending rheometer (BBR)) tests. PVA was added to bitumen at rates of 2%, 4%, 6% and 8% by mass. Based on the bitumen test results, a PVA rate of 6% was selected for the mixture tests. The modification process was carried out at relatively low temperature (150 °C) and mixing time (20 min) based on various trials, considering the short-term aging of the bitumen. With PVA modification, the penetration value of the bitumen decreased while the softening point increased. As a result, the calculated penetration index (PI) increased and the thermal sensitivity of the bitumen decreased. Significant improvements were detected in elastic recovery and force-ductility tests. Additionally, PVA improved the resistance of asphalt to settling and cracking. Similar results were observed in the DSR and BBR tests. Furthermore, the stripping resistance increased and the stability value improved significantly in the mixture tests. Full article
(This article belongs to the Special Issue Innovative Materials and Technologies for Road Pavements)
Show Figures

Figure 1

Figure 1
<p>Flow diagram of the experimental procedure.</p>
Full article ">Figure 2
<p>Aggregate gradation for Marshall specimens and gradation limits.</p>
Full article ">Figure 3
<p>Viscosity test results of the base and modified bitumen; 135 °C, 150 °C and 165 °C.</p>
Full article ">Figure 4
<p>The variation of viscosity results of base and modified bitumens with temperature.</p>
Full article ">Figure 5
<p>Penetration test results.</p>
Full article ">Figure 6
<p>Softening point test results.</p>
Full article ">Figure 7
<p>G*/Sinδ values for unaged original and PVA modified bitumens.</p>
Full article ">Figure 8
<p>G*/Sinδ values for original and PVA-modified bitumens after RTFOT.</p>
Full article ">Figure 9
<p>G*·Sinδ values for original and PVA-modified bitumens after PAV.</p>
Full article ">Figure 10
<p>Nicholson stripping test results; (<b>a</b>) with base bitumen (<b>b</b>) with 6% PVA-modified bitumen.</p>
Full article ">
14 pages, 3565 KiB  
Article
Microstructure and Properties of Ti-5Al-2.5Sn Alloy with Higher Carbon Content
by Agnieszka Szkliniarz and Wojciech Szkliniarz
Coatings 2025, 15(2), 224; https://doi.org/10.3390/coatings15020224 - 13 Feb 2025
Viewed by 288
Abstract
This study investigates the characteristics of the Ti-5Al-2.5Sn-0.2C alloy, an alpha titanium alloy containing approximately 0.2 wt% carbon—a concentration significantly exceeding the standard allowable limit of 0.08 wt%. The Ti-5Al-2.5Sn-0.2C alloy was melted in a vacuum induction furnace with a cold copper crucible, [...] Read more.
This study investigates the characteristics of the Ti-5Al-2.5Sn-0.2C alloy, an alpha titanium alloy containing approximately 0.2 wt% carbon—a concentration significantly exceeding the standard allowable limit of 0.08 wt%. The Ti-5Al-2.5Sn-0.2C alloy was melted in a vacuum induction furnace with a cold copper crucible, processed into bar form through hot rolling, and subsequently annealed under standard conditions. The microstructure and mechanical properties of the Ti-5Al-2.5Sn-0.2C alloy were systematically compared with those of the Ti-5Al-2.5Sn alloy (Grade 6), which possesses a similar chemical composition. The results revealed that the addition of 0.2 wt% carbon significantly influences the alloy’s solidification process, phase transformation temperatures, phase composition, and phase lattice parameters. Moreover, the carbon addition enhances key mechanical properties, including tensile strength, yield strength, hardness, and wear resistance, as well as creep and oxidation resistance. While a slight reduction in plasticity and increase in impact energy were observed, the alloy remained within the permissible range defined by existing standards. Full article
(This article belongs to the Special Issue Advanced Light Metals: Microstructure, Properties, and Applications)
Show Figures

Figure 1

Figure 1
<p>Manufacturing and testing methods of investigated alloys.</p>
Full article ">Figure 2
<p>X-ray diffraction patterns (XRD) of investigated alloys.</p>
Full article ">Figure 3
<p>Microstructure changes during the crystallization process of the Ti-5Al-2.5Sn-0.2C alloy, presented on the background of the Ti-9Al-C phase diagram [based on [<a href="#B34-coatings-15-00224" class="html-bibr">34</a>,<a href="#B35-coatings-15-00224" class="html-bibr">35</a>]].</p>
Full article ">Figure 4
<p>Microstructure of the Ti-5Al-2.5Sn-0.2C alloy after homogenization (<b>a</b>) and hot rolling (<b>b</b>).</p>
Full article ">Figure 5
<p>Microstructure of the Ti-5Al-2.5Sn-0.2C (<b>a</b>) and Ti-5Al-2.5Sn (<b>b</b>) alloy after annealing.</p>
Full article ">Figure 6
<p>Effect of carbon on the creep curves of the Ti-5Al-2.5Sn alloy.</p>
Full article ">Figure 7
<p>Effect of carbon on the oxidation kinetics of the Ti-5Al-2.5Sn alloy.</p>
Full article ">Figure 8
<p>Effect of carbon on the polarization curves of the Ti-5Al-2.5Sn alloy.</p>
Full article ">
20 pages, 8786 KiB  
Article
Experimental Investigation of the Influence of Milling Conditions on Residual Stress in the Surface Layer of an Aerospace Aluminum Alloy
by Magdalena Zawada-Michałowska, Kamil Anasiewicz, Jarosław Korpysa and Paweł Pieśko
Materials 2025, 18(4), 811; https://doi.org/10.3390/ma18040811 - 12 Feb 2025
Viewed by 383
Abstract
In this study, the correlations between milling conditions—namely, the cutting tool feed direction relative to the rolling direction, the milling type, the coolant application, as well as the cutting speed—and the surface residual stress of a selected aluminum alloy (2024 T351) were investigated. [...] Read more.
In this study, the correlations between milling conditions—namely, the cutting tool feed direction relative to the rolling direction, the milling type, the coolant application, as well as the cutting speed—and the surface residual stress of a selected aluminum alloy (2024 T351) were investigated. Determining the type and magnitude of residual stress is of paramount importance as this stress is among the primary causes of post-machining strain of thin-walled components. On the basis of the experimental results, it was found that all factors analyzed significantly affect the residual stress state. Specifically, milling in the parallel direction induces lower residual tensile stress compared to milling in the perpendicular direction. Analogously, up-milling yields lower tensile residual stress than down-milling, and flood cooling leads to lower tensile residual stress than MQL. It was clearly confirmed that as cutting speed increases, tensile residual stress also increases, but only up to a certain threshold; once the high-speed cutting regime is reached, tensile residual stress begins to decrease. Consequently, the proper selection of milling parameters is a crucial consideration for optimizing machining processes and minimizing machining-induced residual stress. Full article
Show Figures

Figure 1

Figure 1
<p>Research plan.</p>
Full article ">Figure 2
<p>Experimental procedure.</p>
Full article ">Figure 3
<p>Example of the single measurement result of surface residual stress (<span class="html-italic">v<sub>c</sub></span> = 750 m/min, up-milling, MQL, parallel feed direction relative to rolling direction).</p>
Full article ">Figure 4
<p>Comparison of residual stress for parallel and perpendicular cutting tool feed directions relative to rolling direction as a function of cutting speed under up-milling and flood cooling.</p>
Full article ">Figure 5
<p>Comparison of residual stress for parallel and perpendicular cutting tool feed directions relative to rolling direction as a function of cutting speed under down-milling and flood cooling.</p>
Full article ">Figure 6
<p>Comparison of residual stress for parallel and perpendicular cutting tool feed directions relative to rolling direction as a function of cutting speed under up-milling and MQL.</p>
Full article ">Figure 7
<p>Comparison of residual stress for parallel and perpendicular cutting tool feed directions relative to rolling direction as a function of cutting speed under down-milling and MQL.</p>
Full article ">Figure 8
<p>Comparison of residual stress for up and down-milling as a function of cutting speed under perpendicular feed direction relative to rolling direction and flood cooling.</p>
Full article ">Figure 9
<p>Comparison of residual stress for up and down-milling as a function of cutting speed under perpendicular feed direction relative to rolling direction and MQL.</p>
Full article ">Figure 10
<p>Comparison of residual stress for up and down-milling as a function of cutting speed under parallel feed direction relative to rolling direction and flood cooling.</p>
Full article ">Figure 11
<p>Comparison of residual stress for up and down-milling as a function of cutting speed under parallel feed direction relative to rolling direction and MQL.</p>
Full article ">Figure 12
<p>Comparison of residual stress for flood cooling and MQL as a function of cutting speed under perpendicular feed direction relative to rolling direction and up-milling.</p>
Full article ">Figure 13
<p>Comparison of residual stress for flood cooling and MQL as a function of cutting speed under perpendicular feed direction relative to rolling direction and down-milling.</p>
Full article ">Figure 14
<p>Comparison of residual stress for flood cooling and MQL as a function of cutting speed under parallel feed direction relative to rolling direction and up-milling.</p>
Full article ">Figure 15
<p>Comparison of residual stress for flood cooling and MQL as a function of cutting speed under parallel feed direction relative to rolling direction and down-milling.</p>
Full article ">Figure 16
<p>Residual stress as a function of cutting speed with different milling combinations and parallel feed direction of the cutting tool with respect to the rolling direction.</p>
Full article ">Figure 17
<p>Residual stress as a function of cutting speed with different milling combinations and perpendicular feed direction of the cutting tool relative to the rolling direction.</p>
Full article ">Figure 18
<p>Interaction plots for ANOVA.</p>
Full article ">
41 pages, 36866 KiB  
Article
Depositional Architecture of Aggrading Delta Front Distributary Channels and Corresponding Depositional Evolution Process in Ordos Basin: Implications for Deltaic Reservoir Prediction
by Yuhang Huang, Xinghe Yu and Chao Fu
Water 2025, 17(4), 528; https://doi.org/10.3390/w17040528 - 12 Feb 2025
Viewed by 302
Abstract
Distributary channels at the delta front of lacustrine basins play a crucial role in transporting terrigenous sediments and redistributing depositional facies along the basin margin. These channels are also significant reservoirs for oil and gas. This study investigates the Triassic Yanchang Formation in [...] Read more.
Distributary channels at the delta front of lacustrine basins play a crucial role in transporting terrigenous sediments and redistributing depositional facies along the basin margin. These channels are also significant reservoirs for oil and gas. This study investigates the Triassic Yanchang Formation in the Southeastern Ordos Basin (China), emphasizing the sedimentary characteristics, hydrodynamic processes, and evolutionary patterns of delta front distributary channels. Special focus is given to the response of sedimentary filling to paleotopographic changes along the basin margin to enhance reservoir prediction. Through field profiling and quantification of channel morphological parameters, two distinct topographic types were identified: transitions from gentle to steep slopes and from steep to gentle slopes. The findings reveal that the morphology, evolution, and distribution patterns of distributary channels were primarily influenced by the paleotopographic gradient, with sediment grain size playing a supplementary role. Detailed analysis highlights the topographic control on sediment transport mechanisms: in gentle terrain, friction-driven processes dominate (rolling/suspension), whereas in steep terrain, inertial forces prevail (rolling/saltation). Channel architecture correlates strongly with paleotopography: gentle to steep transitions form isolated, vertically stacked sand bodies with thick mouth bars, while steep to gentle transitions produce sheet-like sands with lateral migration features. This study establishes a predictive framework linking slope thresholds to reservoir morphology, offering prioritized targets for hydrocarbon exploration. The methodology is applicable to the margins of lacustrine basins in intracratonic settings, reducing subsurface uncertainty by integrating paleotopographic reconstructions with channel aspect ratios and migration rates. Full article
(This article belongs to the Special Issue Regional Geomorphological Characteristics and Sedimentary Processes)
Show Figures

Figure 1

Figure 1
<p>(<b>A</b>) The location of the Ordos Basin. (<b>B</b>) A schematic map showing the main structural units of the Ordos Basin and the study area’s locations. (<b>C</b>) The geological map displays the locations of the studied outcrops in the Southeast Ordos Basin. The letters O, C, P, T<sub>1</sub>, T<sub>2</sub>, T<sub>3</sub>, J, N, K<sub>1</sub>, and Q represent the following geological strata: Ordovician System, Carboniferous System, Permian System, Lower, Middle and Upper Triassic Series, Jurassic System, Neogene System, Lower Cretaceous Series, and Quaternary System.</p>
Full article ">Figure 2
<p>(<b>A</b>) The Triassic succession of the Southeast Ordos Basin displays the Upper Triassic strata, lithology, and thicknesses of the 10 oil members of the Yanchang Formation (Ch1–10), sedimentary facies, lake-level fluctuations, types of sediment, terrain evolution, and the cycle of base level. (<b>B</b>) The sedimentary environment and distribution characteristics of sand bodies during the Ch7 periods.</p>
Full article ">Figure 3
<p>Lithofacies division of the delta front depositional system in the Ch7 member in the Upper Triassic Yanchang Formation in the Ordos Basin.</p>
Full article ">Figure 4
<p>Photographs illustrating the sandstone and mudstone lithofacies related to bedding structures at Zhujiawan outcrop. (<b>A</b>) Large heterocentric trough cross-stratified sandstone (Sth) overlain by large planar cross-stratified sandstone (Sp), followed by parallel-bedded sandstone (Sh), the channel sand body is located between the horizontally bedded siltstone (Fh) and the massive mudstone (Mm). (<b>B</b>) Large planar cross-stratified sandstone (Sp) overlaid by parallel-bedded sandstone (Sh), which is subsequently followed by fining-upward sandstone (Sg). (<b>C</b>) Heterocentric trough cross-stratified sandstone (Sth) overlain by convolute bedded sandstone (Sc), followed by parallel-bedded sandstone (Sh), and horizontal bedded siltstone (Fh) and mudstone (Mh) beneath erosion surface. (<b>D</b>) Planar cross-stratified sandstone (Sp) overlain by current ripple cross-stratified sandstone (Sr), followed by phytodetritus mudstone (Mp). (<b>E</b>) Lower massive sandstone (Sm) overlain by parallel-bedded sandstone (Sh), with large planar cross-stratified sandstone (Sp) at top. Intermediate phytodetritus mudstone (Mp) contains series of ferric concretions. (<b>F</b>) Massive sandstone (Sm) overlying horizontal bedded siltstone (Fh) and horizontal bedded mudstone (Mh). (<b>G</b>) Three mud clasts visible in upper part of fining-upward sandstone (Sg), overlaid by planar cross-stratified sandstone (Sp) and parallel-bedded sandstone (Sh). (<b>H</b>) Phytodetritus observed on plane of sandstone layer. See lithofacies codes in <a href="#water-17-00528-f003" class="html-fig">Figure 3</a> and <a href="#water-17-00528-t001" class="html-table">Table 1</a> for further reference.</p>
Full article ">Figure 5
<p>Photographs illustrating sandstone, siltstone, and mudstone lithofacies related to bedding structures. (<b>A</b>) Massive mudstone (Mm) overlain by concentric trough cross-stratified sandstone (Stc), followed by planar cross-stratified sandstone (Sp) at Yueliangwan outcrop. (<b>B</b>) Carbonaceous mudstone (Mc) and phytodetritus mudstone (Mp) overlaid by planar cross-stratified sandstone (Sp), followed by concentric trough cross-stratified sandstone (Stc) at Yueliangwan outcrop. (<b>C</b>) Large planar cross-stratified sandstone (Sp) at Yueliangwan outcrop. (<b>D</b>) Massive mudstone (Mm) overlain by planar cross-stratified sandstone (Sp), followed by concentric trough cross-stratified sandstone (Stc), and then massive sandstone (Sm) at Yueliangwan outcrop. (<b>E</b>) Phytodetritus observed on mudstone layer plane. (<b>F</b>) A stem fossil of <span class="html-italic">Neocalamites</span> in sandstone, found at Yueliangwan outcrop. (<b>G</b>) Current ripple cross-stratified siltstone (Fr) at Tielongwan outcrop. (<b>H</b>) Horizontal bedded siltstone (Fh) at Tielongwan outcrop. See lithofacies codes in <a href="#water-17-00528-f003" class="html-fig">Figure 3</a> and <a href="#water-17-00528-t001" class="html-table">Table 1</a> for reference.</p>
Full article ">Figure 6
<p>Photographs showing siltstone and mudstone facies related to bedding structures. (<b>A</b>) Massive mudstone (Mm) is overlain by massive siltstone (Fm) at Tielongwan outcrop. (<b>B</b>) Massive siltstone (Fm) is interbedded with massive mudstone (Mm) and channel siltstone in middle at Tielongwan outcrop. (<b>C</b>) Carbonaceous mudstone (Mc) is interbedded with massive siltstone (Fm) at Tielongwan outcrop. (<b>D</b>) Phytodetritus on carbonaceous mudstone bedding plane at Tielongwan outcrop. (<b>E</b>) Massive siltstone (Fm) is overlain by horizontally bedded mudstone (Mh) at Fudihu outcrop. (<b>F</b>) Massive siltstone (Fm) is interbedded with massive mudstone (Mm) and channel siltstone at top of Fudihu outcrop. (<b>G</b>) Silty curled layers are overlain by mudstone at Fudihu outcrop. (<b>H</b>) Deformed structures are overlain by mudstone at Fudihu outcrop. See lithofacies codes in <a href="#water-17-00528-f003" class="html-fig">Figure 3</a> and <a href="#water-17-00528-t001" class="html-table">Table 1</a> for reference.</p>
Full article ">Figure 7
<p>Lithofacies associations of delta front deposits. LA-1: Major distributary channel. LA-2: Swinging distributary channel. LA-3: Lateral accretion distributary channel. LA-4: Interdistributary bay and overflow deposits. LA-5: Distal bar with terminal distributary channel. LA-6: Terminal distributary channel.</p>
Full article ">Figure 8
<p>Channel morphology and depositional elements. (<b>A</b>) Aggradation channel with erosion base. (<b>B</b>) Swinging channel with erosion base. (<b>C</b>) Lateral accretion channel with erosion base. (<b>D</b>) Filled channel with erosion base.</p>
Full article ">Figure 9
<p>Photographs showing a stem fossil of Neocalamite, phytodetritus, and channels with lithofacies Stc fillings. (<b>A</b>) A section of the Fudihu outcrop. The dotted yellow rectangle indicates the area shown in (<b>B</b>–<b>E</b>). (<b>B</b>) Details of the inset in (<b>A</b>) showing a stem fossil of Neocalamite at the base of the massive sandstone, measuring 20.0 cm in length and 8 cm in diameter. (<b>C</b>) A dark gray mudstone with high carbon content and phytodetritus, found at the base of the section, with particle sizes ranging from 1.0 to 3.5 cm. (<b>D</b>) Gray and white lithofacies Sp. (<b>E</b>) Lithofacies Stc with upward thickening, indicating channel filling with an accelerated deposition rate (Type 1). (<b>F</b>) An analysis of the Yueliangwan outcrop (<b>E</b>). (<b>G</b>) The superposition relationship of sand bodies at the Yueliangwan outcrop.</p>
Full article ">Figure 10
<p>Photographs showing a macro section of the Zhujiawan outcrop. (<b>A</b>) The yellow dotted rectangle indicates the area shown in (<b>B</b>,<b>D</b>). (<b>B</b>) Details of the inset in (<b>A</b>), showing a lateral accretion channel. Evidence of lateral deposition is observed in the gray-white fine sandstone, with down-cut planar cross-bedding indicating lateral deposition. (<b>C</b>) An analysis of the Zhujiawan outcrop in (<b>B</b>). (<b>D</b>) Details of the inset in (<b>A</b>), showing a swinging channel. Two phases of gray and white mouth bar sand bodies are present, with the upper phase overlaid by a banded channel complex. (<b>E</b>) An analysis of the Zhujiawan outcrop in (<b>D</b>). (<b>F</b>) The superposition relationship of sand bodies at the Zhujiawan outcrop.</p>
Full article ">Figure 11
<p>Photographs showing a section of the Tielongwan outcrop. (<b>A</b>) The dotted yellow rectangle indicates the area shown in (<b>B</b>–<b>E</b>). (<b>B</b>) Details of the inset in (<b>A</b>) showing three periods of banded dark-gray and gray siltstone, characterized by a flat bottom and convex top. (<b>C</b>) Phytoclasts, ranging in size from 1.00 to 2.00 cm, are visible in the thick-bedded dark gray mudstone. (<b>D</b>) Lithofacies Fr is visible at the top of the sand body. (<b>E</b>) A terminal distributary channel, measuring 3.70 m in width and 0.32 m in thickness, is visible at the top of the distal bar. (<b>F</b>) An analysis of the Tielongwan outcrop shown in (<b>E</b>).</p>
Full article ">Figure 12
<p>Photographs showing a section of the Fudihu outcrop. (<b>A</b>) The dotted yellow rectangle indicates the picture shown in (<b>B</b>,<b>C</b>). (<b>B</b>) Details of the inset in (<b>A</b>) showing silty curled layers covered by mudstone. (<b>C</b>) Details of the inset in (<b>A</b>) showing deformed structures covered by mudstone. (<b>D</b>) The convex lenticular silty sand body at the top of the flat bottom represents the terminal distributary channels, filled with massive siltstone. (<b>E</b>) An analysis of the section of the Fudihu outcrop (<b>D</b>). (<b>F</b>) The superposition relationship of sand bodies in the Fudihu outcrop.</p>
Full article ">Figure 13
<p>The characteristic parameters (<b>A</b>), width-to-thickness ratio (<b>B</b>), degree of symmetry (<b>C</b>), migration frequency (<b>D</b>), sand content rate (<b>E</b>), and relative paleoslope (<b>F</b>) of the channel sand body in the Ch7 upper members in the Upper Triassic Yanchang Formation in the Ordos Basin.</p>
Full article ">Figure 14
<p>A simple evolutional model of the distributary channels. The study area’s delta front is classified into three sections based on facies zone and topography to explain the evolution of four types of distributary channels.</p>
Full article ">
14 pages, 6418 KiB  
Article
Dynamic and Static Strength Analysis of 5056 Aluminum Alloy Fabricated by Wire-Arc Additive Manufacturing
by Alexey Evstifeev, Aydar Mavlyutov, Darya Volosevich, Marina Gushchina, Olga Klimova-Korsmik, Konstantin Nasonovskiy and Sofya Shabunina
Metals 2025, 15(2), 189; https://doi.org/10.3390/met15020189 - 12 Feb 2025
Viewed by 326
Abstract
This article presents the results of experimental studies on the dynamic and static strength of commercial aluminum alloy 5056 manufactured by wire-arc additive manufacturing (WAAM). The main objective is to evaluate the utilization potential of this technology for manufacturing parts for operation under [...] Read more.
This article presents the results of experimental studies on the dynamic and static strength of commercial aluminum alloy 5056 manufactured by wire-arc additive manufacturing (WAAM). The main objective is to evaluate the utilization potential of this technology for manufacturing parts for operation under shock loads. The dynamic tensile strength of the material was investigated with a modified Kolsky method, implemented by a split Hopkinson pressure bar. A comparative analysis of the strength characteristics of materials manufactured by WAAM and conventional cold-rolling methods was carried out using a structurally temporal approach with the incubation time criterion. The results showed that the aluminum alloy obtained by WAAM demonstrates comparable strength levels to that of cold-rolled material. The findings suggest that WAAM can be a competitive alternative for producing high-strength aluminum alloys for operation under shock loads. Full article
Show Figures

Graphical abstract

Graphical abstract
Full article ">Figure 1
<p>Scheme of a WAAM setup (<b>a</b>); the photo of AA5056_AM (<b>b</b>).</p>
Full article ">Figure 2
<p>The scheme of experimental tension test setup with SHPB.</p>
Full article ">Figure 3
<p>Backscattered electrons micrograph of (<b>a</b>) AA5056_IM and (<b>b</b>) AA5056_AM; (<b>c</b>) cross-sectional EBSD maps of AA5056_IM; (<b>d</b>) cross-sectional EBSD maps of AA5056_AM; 1–6 are the areas for EDS analysis.</p>
Full article ">Figure 4
<p>Fracture surface after tension test of AA5056_IM (<b>a</b>–<b>c</b>) and AA5056_AM (<b>d</b>–<b>f</b>). The Al6(Fe,Mn) particles are indicated by arrows on (<b>c</b>,<b>f</b>). The samples are marked (*) in <a href="#metals-15-00189-f007" class="html-fig">Figure 7</a>.</p>
Full article ">Figure 5
<p>Stress-time curves for AA5056_IM (<b>a</b>) and AA5056_AM (<b>b</b>), obtained under dynamic tension loads.</p>
Full article ">Figure 6
<p>Fracture surface after tension test of AA5056_IM (<b>a</b>–<b>c</b>) and AA5056_AM (<b>d</b>–<b>f</b>) on the split Hopkinson pressure bar. The Al6(Fe,Mn) particles are indicated by arrows. The samples are marked (**) in <a href="#metals-15-00189-f007" class="html-fig">Figure 7</a>.</p>
Full article ">Figure 7
<p>Experimental and calculated dependences of the maximum tensile strength on the stress rates ofAA5056_IM and AA5056_AM. The markers are experimental data, the curves are plotted according to criterion (1) considering the material parameters from <a href="#metals-15-00189-t004" class="html-table">Table 4</a>. Samples for surface fracture investigations after tension at static (*) and dynamic (**) modes.</p>
Full article ">
Back to TopTop