Nothing Special   »   [go: up one dir, main page]

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

Article Types

Countries / Regions

remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline

Search Results (1,721)

Search Parameters:
Keywords = slip effect

Order results
Result details
Results per page
Select all
Export citation of selected articles as:
20 pages, 2128 KiB  
Article
Analytical Solutions for Electroosmotic Flow and Heat Transfer Characteristics of Nanofluids in Circular Cylindrical Microchannels with Slip-Dependent Zeta Potential Considering Thermal Radiative Effects
by Zouqing Tan and Xiangcheng Ren
Micromachines 2025, 16(1), 63; https://doi.org/10.3390/mi16010063 (registering DOI) - 5 Jan 2025
Abstract
This study analyzes the impact of slip-dependent zeta potential on the heat transfer characteristics of nanofluids in cylindrical microchannels with consideration of thermal radiation effects. An analytical model is developed, accounting for the coupling between surface potential and interfacial slip. The linearized Poisson–Boltzmann [...] Read more.
This study analyzes the impact of slip-dependent zeta potential on the heat transfer characteristics of nanofluids in cylindrical microchannels with consideration of thermal radiation effects. An analytical model is developed, accounting for the coupling between surface potential and interfacial slip. The linearized Poisson–Boltzmann equation, along with the momentum and energy conservation equations, is solved analytically to obtain the electrical potential field, velocity field, temperature distribution, and Nusselt number for both slip-dependent (SD) and slip-independent (SI) zeta potentials. Subsequently, the effects of key parameters, including electric double-layer (EDL) thickness, slip length, nanoparticle volume fraction, thermal radiation parameters, and Brinkman number, on the velocity field, temperature field, and Nusselt number are discussed. The results show that the velocity is consistently higher for the SD zeta potential compared to the SI zeta potential. Meanwhile, the temperature for the SD case is higher than that for the SI case at lower Brinkman numbers, particularly for a thinner EDL. However, an inverse trend is observed at higher Brinkman numbers. Similar trends are observed for the Nusselt number under both SD and SI zeta potential conditions at different Brinkman numbers. Furthermore, for a thinner EDL, the differences in flow velocity, temperature, and Nusselt number between the SD and SI conditions are more pronounced. Full article
(This article belongs to the Section C1: Micro/Nanoscale Electrokinetics)
19 pages, 1637 KiB  
Article
Analysis of Energy Dissipation and Sealing Performance of the Premium Connection in Modal Vibrations
by Yang Yu, Yang Liu, Yinping Cao, Qingying Yuan, Jiarui Tang and Yihua Dou
Appl. Sci. 2025, 15(1), 393; https://doi.org/10.3390/app15010393 - 3 Jan 2025
Viewed by 302
Abstract
Traditional static analysis cannot effectively explain the issue of the sealing performance of the premium connection being decreased due to the vibration of the tubing, leading to the failure of the connection sealing. In this paper, based on the energy dissipation theory and [...] Read more.
Traditional static analysis cannot effectively explain the issue of the sealing performance of the premium connection being decreased due to the vibration of the tubing, leading to the failure of the connection sealing. In this paper, based on the energy dissipation theory and considering the influence of the micro contact slip of the sealing surface under the vibration of the tubing, a finite element model of the premium connection is established. The natural frequency and vibration mode are obtained through modal analysis experiments, and the accuracy of the finite element model is verified. The results show that the first five natural frequencies are mainly concentrated in the axial direction of the tubing, with the amplitude of the radial vibration mode being small. The vibration mode results are applied to the model as boundary conditions. It is found that an increase in the axial displacement amplitude leads to an increase in the energy dissipation of the sealing surface of the premium connection, which reduces the normal contact pressure and the effective length of the sealing surface, ultimately leading to a decrease in the sealing performance. Full article
23 pages, 15720 KiB  
Article
Composite Sorbents Based on Chitosan Polymer Matrix and Derivatives of 4-Amino-N′-hydroxy-1,2,5-oxadiazole-3-carboximidamide for Uranium Removal from Liquid Mineralized Media
by Anna I. Matskevich, Konstantin V. Maslov, Veronika A. Prokudina, Daria D. Churakova, Oleg Yu. Slabko, Dmitry K. Patrushev, Nikita S. Markin and Eduard A. Tokar’
Gels 2025, 11(1), 24; https://doi.org/10.3390/gels11010024 - 1 Jan 2025
Viewed by 385
Abstract
Composite adsorbents based on a natural biopolymer matrix of chitosan, to which 4-amino-N′-hydroxy-1,2,5-oxadiazole-3-carboximidamide and its Se derivative were attached, were synthesized. A complex of physicochemical analysis methods indicates that the direct introduction of a matrix with high ionic permeability into the reaction mixture [...] Read more.
Composite adsorbents based on a natural biopolymer matrix of chitosan, to which 4-amino-N′-hydroxy-1,2,5-oxadiazole-3-carboximidamide and its Se derivative were attached, were synthesized. A complex of physicochemical analysis methods indicates that the direct introduction of a matrix with high ionic permeability into the reaction mixture contributes to the formation of homogeneous particles of composite with developed surface morphology, which enhances the kinetic and capacitive parameters of uranium sorption in liquid media. It has been established that the direct introduction of a matrix with high ionic permeability into the reaction mixture contributes to the formation of homogeneous particles with a developed surface morphology, which enhances the kinetic and capacitive parameters of uranium sorption in liquid media. The synthesized materials had increased sorption-selective properties towards uranium in the pH range from 4 to 9 under static sorption conditions. The formation of the Se derivative of amidoxime during its attachment to the polymer matrix (Se-chit) contributes to the creation of a more chemically stable and highly effective adsorbent, compared to the direct binding of 4-amino-N′-hydroxy-1,2,5-oxadiazole-3-carboximidamide with chitosan (43AF-chit). The optimal parameters for the synthesis of materials were established. It was demonstrated that the ratio of amidoxime to chitosan should be within the range of 2:1 to 1:2. As the mass content of chitosan increases, the material gradually dissolves and transforms into a gel, resulting in the formation of liquid radioactive waste with a complex chemical composition. It was found that the kinetic sorption parameters of composite materials increase 2–10 times compared to those of non-composite materials. The sorption capacity of uranium in solutions with pH 6 and pH 8 can reach approximately 400–450 mg g−1. Under dynamic sorption conditions, the effective filtration cycle values (before uranium slips into the filtrate ≥ 50%) improve significantly when transitioning from a non-composite adsorbent to a composite one: increasing from 50 to 800 b.v. for pH 6 and from 2700 to 4000 b.v. for pH 8. These results indicate that the synthesized sorbents are promising materials for uranium removal from liquid media, suitable for both purification and the recovery of radionuclides as valuable raw materials. Full article
(This article belongs to the Special Issue Eco-Friendly Gels for Adsorption)
Show Figures

Graphical abstract

Graphical abstract
Full article ">Figure 1
<p>IR-spectra of synthesized materials: (<b>a</b>) based on Se derivative of N′-hydroxy-1,2,5-oxadiazole-3-carboximidamide (Se-chit (x/y)), (<b>b</b>) based on N′-hydroxy-1,2,5-oxadiazole-3-carboximidamide (43AF–chit(x)).</p>
Full article ">Figure 2
<p>Diffractograms of synthesized materials: (<b>a</b>) based on Se derivative of N′-hydroxy-1,2,5-oxadiazole-3-carboximidamide (Se-chit (x/y)), (<b>b</b>) based on N′-hydroxy-1,2,5-oxadiazole-3-carboximidamide (43AF–chit(x)).</p>
Full article ">Figure 3
<p>SEM-images of synthesized materials: (<b>a</b>–<b>c</b>) based on Se derivative of N′-hydroxy-1,2,5-oxadiazole-3-carboximidamide (Se-chit (x/y)), (<b>d</b>–<b>f</b>) based on N′-hydroxy-1,2,5-oxadiazole-3-carboximidamide (43AF–chit (x)).</p>
Full article ">Figure 4
<p>The results of EDX analysis of composite materials: (<b>a</b>) Se-chit (1/1), (<b>b</b>) 43-AF-chit (25%).</p>
Full article ">Figure 5
<p>The scheme of formation of composites based on 4-amino-N′-hydroxy-1,2,5-oxadiazole-3-carboximidamide (43AF-chit (x)).</p>
Full article ">Figure 6
<p>The scheme of formation of composites based on Se derivative of 4-amino-N′-hydroxy-1,2,5-oxadiazole-3-carboximidamide (Se-chit (1/1)).</p>
Full article ">Figure 7
<p>Thermograms of composite materials of the series: (<b>a</b>) Se-chit (1/1), (<b>b</b>) Se-chit (1/2), (<b>c</b>) Se-chit (1/4), (<b>d</b>) Se-chit (1/6).</p>
Full article ">Figure 8
<p>Thermograms of composite materials of the series: (<b>a</b>) 43AF-chit (5), (<b>b</b>) 43AF-chit (15), (<b>c</b>) 43AF-chit (25).</p>
Full article ">Figure 9
<p>Relationship between the efficiency of uranium removal from 0.1 M NaNO<sub>3</sub> solutions at pH 6 and the curing temperature of the composites (V:m = 1000 mL g<sup>−1</sup>).</p>
Full article ">Figure 10
<p>Distribution coefficients for uranium across different ratios of sorption-active components and matrix at varying pH levels: (<b>a</b>) adsorbents from the 43AF-chit (x) series; (<b>b</b>) adsorbents from the Se-chit (x/y) series, cured at 60 °C and 120 °C, respectively (ratio V:m = 1000 mL g<sup>−1</sup>).</p>
Full article ">Figure 11
<p>Dependence of the static exchange capacity of uranium on the type and concentration of competing anions in solutions: (<b>a</b>,<b>d</b>) pH 4, (<b>b</b>,<b>e</b>,<b>h</b>) pH 6, (<b>c</b>,<b>f</b>,<b>i</b>) pH 8; (<b>g</b>) the value of the zero charge point of sorbents (pH<sub>pzc</sub>), (V:m = 1000 mL g<sup>−1</sup>).</p>
Full article ">Figure 12
<p>Isotherms of uranium sorption from model solutions with pH 6 and approximation of the experimental values by the Langmuir, Freundlich, and SIPS equations: (<b>a</b>) Se-init, (<b>b</b>) Se-Hit (2/1), (<b>c</b>) Se-Hit (1/1), (<b>d</b>) Se-Hit (1/2).</p>
Full article ">Figure 13
<p>Dependence of the efficiency of uranium extraction on the type of sorbent for model solutions with: (<b>a</b>) pH 6, (<b>b</b>) pH 8.</p>
Full article ">Figure 14
<p>Sorption of uranium under dynamic conditions from model solutions 0.1 mol L<sup>−1</sup> NaNO<sub>3</sub>, (<b>a</b>) pH 6, (<b>b</b>) pH 8.</p>
Full article ">
15 pages, 8467 KiB  
Case Report
In Situ Fixation and Intertrochanteric Osteotomy for Severe Slipped Capital Femoral Epiphysis Following Femoral Neck Fracture: A Case Report with Application of Virtual Surgical Planning and 3D-Printed Patient-Specific Instruments
by Giovanni Trisolino, Grazia Chiara Menozzi, Alessandro Depaoli, Olaf Stefan Schmidt, Marco Ramella, Marianna Viotto, Marco Todisco, Massimiliano Mosca and Gino Rocca
J. Pers. Med. 2025, 15(1), 13; https://doi.org/10.3390/jpm15010013 - 1 Jan 2025
Viewed by 274
Abstract
Background: Femoral neck fractures are rare but serious injuries in children and adolescents, often resulting from high-energy trauma and prone to complications like avascular necrosis (AVN) and nonunion. Even rarer is the development of slipped capital femoral epiphysis (SCFE) following femoral neck [...] Read more.
Background: Femoral neck fractures are rare but serious injuries in children and adolescents, often resulting from high-energy trauma and prone to complications like avascular necrosis (AVN) and nonunion. Even rarer is the development of slipped capital femoral epiphysis (SCFE) following femoral neck fracture, which presents unique diagnostic and treatment challenges. SCFE can destabilize the femoral head, with severe cases requiring complex surgical interventions. Case presentation: This report details a case of a 15-year-old male with autism spectrum disorder (ASD) who developed severe SCFE one month after treatment for a Delbet type III femoral neck fracture. The condition was managed with an Imhäuser intertrochanteric osteotomy (ITO), in situ fixation (ISF), and osteochondroplasty (OChP), supported by virtual surgical planning (VSP) and 3D-printed patient-specific instruments (PSIs) for precise correction and fixation. Discussion: The surgery was completed without complications. Six months after the operation, the patient exhibited a pain-free, mobile hip with radiographic evidence of fracture healing and no signs of AVN. Functional outcomes were favorable despite rehabilitation challenges due to ASD. Conclusions: The Imhäuser ITO, combined with ISF and OChP, effectively addressed severe SCFE after femoral neck fracture, minimizing AVN risk. VSP and PSIs enhanced surgical accuracy and efficiency, demonstrating their value in treating rare and complex pediatric orthopedic conditions. Full article
(This article belongs to the Special Issue Orthopedic Trauma: New Perspectives and Innovative Techniques)
Show Figures

Figure 1

Figure 1
<p>(<b>a</b>) Radiograph after trauma showing a Delbet Type III femoral neck fracture; (<b>b</b>) radiograph after open reduction and internal fixation surgery; (<b>c</b>) radiograph at one-month follow-up showing signs of mild SCFE (white arrow); (<b>d</b>) radiograph at three-month follow-up showing worsening SCFE (white arrow).</p>
Full article ">Figure 1 Cont.
<p>(<b>a</b>) Radiograph after trauma showing a Delbet Type III femoral neck fracture; (<b>b</b>) radiograph after open reduction and internal fixation surgery; (<b>c</b>) radiograph at one-month follow-up showing signs of mild SCFE (white arrow); (<b>d</b>) radiograph at three-month follow-up showing worsening SCFE (white arrow).</p>
Full article ">Figure 2
<p>(<b>a</b>) Overlap of the healthy contralateral femur (shown in green with an orange outline); (<b>b</b>) Identification of a plane tangent to the base of the slipped epiphysis and of the position of the screw for ISF (outlined in orange).</p>
Full article ">Figure 3
<p>(<b>a</b>) The first step was to determine the final position of the proximal femur after an intertrochanteric closing wedge and derotative osteotomy in order to improve the range of motion of the hip; (<b>b</b>) final positioning of the 90° blade plate; (<b>c</b>) the plate (highlighted in orange) was positioned in order to avoid the holes of the previous hardware (in dark gray) as much as possible; (<b>d</b>) restoring the femur to its deformed state maintaining the plate in its position relative to the proximal femur reveals the initial position of the blade and the shape of the bone wedge that needs to be removed (in red).</p>
Full article ">Figure 4
<p>(<b>a</b>) Anterior view of the proximal femur with the initial plate positioning and the bone wedge to remove; (<b>b</b>) positioning of the guidewire for the cannulated screw (the more anterior wire) and two lateral wires for the placement of the blade plate; (<b>c</b>) design of the first 3D-printed PSI (highlighted in light blue).</p>
Full article ">Figure 5
<p>(<b>a</b>) The position of the chisel along the proximal 1.5 mm guidewire and of the distal 1.5 mm guidewire; (<b>b</b>) the second PSI(highlighted in light blue), designed to fit onto the distal guidewire, precisely indicates the directions for chisel insertion and for the distal cut; (<b>c</b>) design of the third PSI (highlighted in light blue), featuring similar characteristics to the second, but specifically guiding the proximal cut; (<b>d</b>) simulated correction in valgus, flexion, and internal rotation of the distal femur.</p>
Full article ">Figure 6
<p>The final 3D-printed samples of the PSIs. From the left to the right: the first PSI for wire positioning, the second PSI for the distal cut, and the third PSI for the proximal cut.</p>
Full article ">Figure 7
<p>(<b>a</b>) Anatomical landmarks and fluoroscopy check; (<b>b</b>) L-incision along the proximal inferior border of the vastus lateralis; (<b>c</b>) removal of the DHS plate and of the proximal anti-rotation screw.</p>
Full article ">Figure 8
<p>The intraoperative application of the first PSI. (<b>a</b>) Intraoperative picture of the first PSI in place; (<b>b</b>) intraoperative imaging of guidewire positioning; (<b>c</b>) position of guidewires for the free screw for ISF (highlighted in yellow) and for the blade plate (highlighted in orange) in the VSP for comparison with the intraoperative imaging.</p>
Full article ">Figure 9
<p>The intraoperative application of the second PSI. (<b>a</b>) The distal 1.5 mm guidewire was leveraged to precisely fit the second PSI; (<b>b</b>) a longitudinal line was marked to monitor rotational alignment.</p>
Full article ">Figure 10
<p>The intraoperative application of the third PSI. (<b>a</b>) Application of the third cutting guide on the previously inserted guidewire; (<b>b</b>) application of the third guide to set the correct angulation of the chisel.</p>
Full article ">Figure 11
<p>(<b>a</b>) Intraoperative fluoroscopy showing the anterior bump; (<b>b</b>) intraoperative fluoroscopy showing the bump removal after the OChP (fine needle marks the area of the resected bump).</p>
Full article ">Figure 12
<p>Radiographs at 6 months follow-up. (<b>a</b>) Anteroposterior view; (<b>b</b>) frog-leg view.</p>
Full article ">
16 pages, 9500 KiB  
Article
Effect of Soil Type on Running Performance of Small Lunar Rover
by Kimitaka Watanabe, Tomoki Horiguchi and Kazuto Tanaka
Aerospace 2025, 12(1), 24; https://doi.org/10.3390/aerospace12010024 - 31 Dec 2024
Viewed by 256
Abstract
It is very easy for a small lunar rover to slip on the regolith of the lunar surface and become stuck. Previous studies have quantitatively evaluated the effects of wheel geometry, such as elliptical or eccentric wheels, on the performance of a rover [...] Read more.
It is very easy for a small lunar rover to slip on the regolith of the lunar surface and become stuck. Previous studies have quantitatively evaluated the effects of wheel geometry, such as elliptical or eccentric wheels, on the performance of a rover when climbing up slopes. These studies reported that the rovers were able to run on a 30-degree slope made of silica sand. In this study, a small rover was designed and created, and running tests were conducted using lunar soil simulant and silica sand to predict its performance on the lunar surface. The effects of soil differences on the performance of the rover were clarified through the running tests and the measurement of reaction force on the lug. Although the rover exhibited a greater slip ratio on the lunar soil simulant than on the silica sand, the rover with eccentric wheels was able to climb up to a 30-degree angle on the lunar soil simulant. The results for the sinkage measurement of the rover showed that the eccentric wheels prevented sinkage with their up-and-down motion, enabling the rover to climb steep slopes. Furthermore, the tests for measuring the reaction force on the lug indicated that the density change in the lunar soil simulant did not provide sufficient reaction force, and that the running performance on the lunar soil simulant was lower than that on the silica sand. Full article
(This article belongs to the Section Astronautics & Space Science)
Show Figures

Figure 1

Figure 1
<p>Observed soil images: (<b>a</b>) silica sand; (<b>b</b>) lunar soil simulant.</p>
Full article ">Figure 2
<p>Method of Feret diameter measurement.</p>
Full article ">Figure 3
<p>Particle size.</p>
Full article ">Figure 4
<p>Device for measuring reaction force that the lug receives from soil.</p>
Full article ">Figure 5
<p>Schematic diagram of the test to measure reaction force that the lug receives from soil.</p>
Full article ">Figure 6
<p>Test to measure reaction force that the lug receives from soil.</p>
Full article ">Figure 7
<p>Appearance of the rover.</p>
Full article ">Figure 8
<p>Drawings of wheels: (<b>a</b>) circular wheel; (<b>b</b>) elliptical wheel; (<b>c</b>) eccentric wheel.</p>
Full article ">Figure 9
<p>Drawing of small rover.</p>
Full article ">Figure 10
<p>Running test field for silica sand.</p>
Full article ">Figure 11
<p>Running test field for lunar soil simulant: (<b>a</b>) tilting mechanism; (<b>b</b>) appearance.</p>
Full article ">Figure 12
<p>Schematic diagram of running test: (<b>a</b>) silica sand; (<b>b</b>) lunar soil simulant.</p>
Full article ">Figure 13
<p>Relationship between density and shear torque.</p>
Full article ">Figure 14
<p>Non-contact 3D displacement and strain measurement system (ARAMIS).</p>
Full article ">Figure 15
<p>Rover affixed with six dedicated reflective stickers to the top surface and four to the sides.</p>
Full article ">Figure 16
<p>Reaction force on the lug.</p>
Full article ">Figure 17
<p>Observed images at one second after the start of arm drive in a test for measuring the reaction force of the lug with the robot arm.</p>
Full article ">Figure 18
<p>Running time: (<b>a</b>) circular wheel; (<b>b</b>) elliptical wheel; (<b>c</b>) eccentric wheel.</p>
Full article ">Figure 19
<p>Slip ratio: (<b>a</b>) circular wheel; (<b>b</b>) elliptical wheel; (<b>c</b>) eccentric wheel.</p>
Full article ">Figure 20
<p>Images observed by the 3D scanner during running: (<b>a</b>) silica sand; (<b>b</b>) lunar soil simulant.</p>
Full article ">Figure 21
<p>‘After-sliding’ angle of slope.</p>
Full article ">Figure 22
<p>Sinkage (20 degrees): (<b>a</b>) circular wheel; (<b>b</b>) elliptical wheel; (<b>c</b>) eccentric wheel.</p>
Full article ">Figure 22 Cont.
<p>Sinkage (20 degrees): (<b>a</b>) circular wheel; (<b>b</b>) elliptical wheel; (<b>c</b>) eccentric wheel.</p>
Full article ">Figure 23
<p>Interactive model between wheel and soil on slope.</p>
Full article ">Figure 24
<p>Mechanism of sinking.</p>
Full article ">Figure 25
<p>Overlapping diagram of each wheel.</p>
Full article ">
27 pages, 7982 KiB  
Article
Contact Dynamic Behaviors of Magnetic Hydrogel Soft Robots
by Yunian Shen and Yiming Zou
Gels 2025, 11(1), 20; https://doi.org/10.3390/gels11010020 (registering DOI) - 31 Dec 2024
Viewed by 250
Abstract
Magnetic hydrogel soft robots have shown great potential in various fields. However, their contact dynamic behaviors are complex, considering stick–slip motion at the contact interface, and lack accurate computational models to analyze them. This paper improves the numerical computational method for hydrogel materials [...] Read more.
Magnetic hydrogel soft robots have shown great potential in various fields. However, their contact dynamic behaviors are complex, considering stick–slip motion at the contact interface, and lack accurate computational models to analyze them. This paper improves the numerical computational method for hydrogel materials with magneto-mechanical coupling effect, analyses the inchworm-like contact motion of the biomimetic bipedal magnetic hydrogel soft robot, and designs and optimizes the robot’s structure. In the constitutive model, a correction factor representing the influence of the direction of magnetic flux density on the domain density has been introduced. The magnetic part of the Helmholtz free energy has been redefined as the magnetic potential energy, which can be used to explain the phenomenon that the material will still deform when the magnetic flux density is parallel to the external magnetic field. The accuracy of the simulation is verified by comparing numerical solutions with experimental results for a magnetic hydrogel cantilever beam. Furthermore, employing the present methods, the locomotion of a magnetic hydrogel soft robot modeled after the inchworm’s gait is simulated, and the influence of the coefficient of friction on its movement is discussed. The numerical results clearly display the control effect of the external magnetic field on the robot’s motion. Full article
Show Figures

Figure 1

Figure 1
<p>Magnetic hysteresis loops of magnetic materials along certain direction (where <span class="html-italic">H</span> represents the projection of the magnetic field strength <b>H</b>, <span class="html-italic">B</span> represents the projection of the magnetic flux density <b>B</b>, <span class="html-italic">B</span> represents the projection of the coercivity <b>H</b><sup>c</sup>, <span class="html-italic">B</span><sup>m</sup> represents the projection of the saturation magnetic flux density <b>B</b><sup>m</sup>, and <span class="html-italic">B</span><sup>r</sup> represents the projection of the remanence of <b>B</b><sup>r</sup> along a certain direction).</p>
Full article ">Figure 2
<p>Schematic diagram of material line elements.</p>
Full article ">Figure 3
<p>Schematic diagram of the variation of magnetic domain density with the deformation of magnetic hydrogel.</p>
Full article ">Figure 4
<p>Curve of the rate of change of magnetic flux density <math display="inline"><semantics> <mrow> <msup> <mi>λ</mi> <mi mathvariant="normal">m</mi> </msup> </mrow> </semantics></math> versus the material stretch ratio <math display="inline"><semantics> <mrow> <msub> <mi>λ</mi> <mi>z</mi> </msub> </mrow> </semantics></math> in the same direction.</p>
Full article ">Figure 5
<p>Micro-element of equivalent continuum body.</p>
Full article ">Figure 6
<p>Uniaxial extension and compression of a cubic of magnetic hydrogel.</p>
Full article ">Figure 7
<p>Numerical solutions for displacement contour of the magnetic hydrogel cube in the <span class="html-italic">z</span> direction. (<b>a</b>) Initial undeformed state with no external magnetic field; (<b>b</b>) compressed deformation under the action of an external magnetic field (<span class="html-italic">λ<sub>z</sub></span> = 0.83); (<b>c</b>) extension state under the action of an external magnetic field (<span class="html-italic">λ<sub>z</sub></span> = 1.22).</p>
Full article ">Figure 8
<p>Uniaxial extension and compression of the magnetic hydrogel cube in the magnetic field.</p>
Full article ">Figure 9
<p>Schematic diagram of the magnetic hydrogel cantilever beam under the magnetic field force.</p>
Full article ">Figure 10
<p>Bending of the hydrogel cantilever beam: (<b>a</b>) deflection of the magnetic polyvinyl alcohol (PVA) hydrogel cantilever beam in the experiment under 30 mT; (<b>b</b>) deflection of the magnetic PVA hydrogel cantilever beam in the simulation under 30 mT; (<b>c</b>) comparison of experimental, theoretical, and simulation deflection results of the magnetic PVA cantilever beam under different external magnetic induction intensities.</p>
Full article ">Figure 11
<p>Schematic diagram of the double-feet magnetic hydrogel soft robot.</p>
Full article ">Figure 12
<p>Deformation and force of the designed bipedal magnetic hydrogel soft robot under the magnetic field. (<b>a</b>) The initial configuration of the soft robot, L is the foot length, is half of the foot angle, <b>B</b><sup>r</sup> is the residual magnetic flux density of the material, <b>B</b> is the magnetic flux density of the material in the instantaneous configuration, <math display="inline"><semantics> <mrow> <msup> <mstyle mathvariant="bold" mathsize="normal"> <mi>B</mi> </mstyle> <mrow> <mi>applied</mi> </mrow> </msup> </mrow> </semantics></math> is the external magnetic field strength applied, M is the center point of the structure, P is the contact point; (<b>b</b>) under the external magnetic field strength in the x-direction, the bipedal structure bends inward, and at this time, due to the different bending deflections of each point on the foot length, each point B is also different, thus generating different directions of forces on the two feet under the external magnetic field strength in the <span class="html-italic">z</span>-direction, and the rear foot lifts off the contact surface.</p>
Full article ">Figure 13
<p>Variation of magnetic field strength loads in the <span class="html-italic">x</span> and <span class="html-italic">z</span> directions over time.</p>
Full article ">Figure 14
<p>Schematic diagram of the magnetic bipedal hydrogel soft robot structure (where <span class="html-italic">W</span> is the width, <span class="html-italic">L</span> is the foot length, and <span class="html-italic">c</span> is the thickness).</p>
Full article ">Figure 15
<p>Model used for parameterized optimization.</p>
Full article ">Figure 16
<p>Displacement of the end of the foot structure in the <span class="html-italic">x</span>-direction for different peak values of magnetic field load of 80~240 mT and 1/2 bipedal angles of 20–55°.</p>
Full article ">Figure 17
<p>Schematic diagram of the soft robot’s motion within one cycle (Von Mises stress contour) compared with the motion of the inchworm. (<b>a</b>) The rear foot leaves the contact surface at 0.55 s; (<b>b</b>) the two feet complete the inward bending at 1.32 s; (<b>c</b>) the front foot leaves the contact surface at 2.33 s; (<b>d</b>) the motion cycle is completed.</p>
Full article ">Figure 18
<p>Displacement of the soft robot’s center point M in the <span class="html-italic">x</span> and <span class="html-italic">z</span> directions within one cycle.</p>
Full article ">Figure 19
<p>Velocity of the soft robot’s center point M in the <span class="html-italic">x</span> and <span class="html-italic">z</span> directions within one cycle.</p>
Full article ">Figure 20
<p>Time history of the displacement of the soft robot’s center point M in the <span class="html-italic">x</span> direction under different coefficients of friction.</p>
Full article ">
10 pages, 8429 KiB  
Article
Study on Fatigue Fracture Behavior of S32750 Duplex Stainless Steel at Different Solution Temperatures
by Shun Bao, Han Feng, Zhigang Song, Jianguo He, Xiaohan Wu and Yang Gu
Crystals 2025, 15(1), 44; https://doi.org/10.3390/cryst15010044 - 31 Dec 2024
Viewed by 232
Abstract
This paper investigates the tensile and low-cycle fatigue characteristics of S32750 duplex stainless steel subjected to two distinct solid solution treatment temperatures. The microstructures, fracture surfaces, and slip systems of the tested steel were analyzed using optical microscopy (OM), scanning electron microscopy (SEM), [...] Read more.
This paper investigates the tensile and low-cycle fatigue characteristics of S32750 duplex stainless steel subjected to two distinct solid solution treatment temperatures. The microstructures, fracture surfaces, and slip systems of the tested steel were analyzed using optical microscopy (OM), scanning electron microscopy (SEM), and transmission electron microscopy (TEM) techniques. The findings reveal that elevating the solid solution treatment temperature from 1080 °C to 1180 °C results in an increase in the yield strength of the tested steel by approximately 36 MPa and a substantial enhancement in fatigue life by 34%. Microhardness measurements indicate that the degree of hardening in austenite post-fatigue failure significantly surpasses that of ferrite. The variation in solid solution temperature alters the ferrite and austenite content within the matrix, consequently affecting the strain distribution between the two phases. The high-temperature solid solution treatment effectively enhances the two-phase strain-bearing capacity of the tested steel. Following the 1180 °C solid solution treatment, no cloud-like dislocation patterns were observed in the ferrite; instead, they were replaced by a proliferation of thick, interwoven dislocation bundles. In contrast, the dislocations within the austenite predominantly consist of ordered planar slip and twinning. The primary contributor to the extended fatigue life is the increased number of absorbed dislocations within the ferrite grains. Full article
(This article belongs to the Special Issue Advanced High-Strength Steel)
Show Figures

Figure 1

Figure 1
<p>Relationship between phase content change and temperature in test steel.</p>
Full article ">Figure 2
<p>Sampling direction and dimensions of fatigue (<b>a</b>) and tensile (<b>b</b>) specimens.</p>
Full article ">Figure 3
<p>Microstructure morphology: (<b>a</b>) the distribution and morphology of inclusions in the matrix; (<b>b</b>) two-phase morphology after solid solution at 1080 °C; (<b>c</b>) two-phase morphology after solid solution at 1180 °C.</p>
Full article ">Figure 4
<p>Fracture morphology at different solution temperatures: 1080 °C: (<b>a</b>–<b>c</b>); 1180 °C: (<b>d</b>–<b>f</b>).</p>
Full article ">Figure 5
<p>Fatigue life and two-phase microhardness. Test the fatigue life of steel: (<b>a</b>); Ferrite Microhardness change of ferrite: (<b>b</b>); Microhardness change of austenite: (<b>c</b>).</p>
Full article ">Figure 6
<p>Dislocation morphology of two-phase after solution treatment at 1080 °C: (<b>a</b>–<b>d</b>) ferrite dislocation; (<b>e</b>,<b>f</b>) austenite dislocation.</p>
Full article ">Figure 7
<p>Dislocation morphology of two-phase after solution treatment at 1180 °C: (<b>a</b>–<b>d</b>) ferrite dislocation; (<b>e</b>–<b>h</b>) austenite dislocation.</p>
Full article ">
29 pages, 9091 KiB  
Article
Estimation Strategy for the Adhesion Coefficient of Arbitrary Pavements Based on an Optimal Adaptive Fusion Algorithm
by Zhiwei Xu, Jianxi Wang, Yongjie Lu and Haoyu Li
Machines 2025, 13(1), 17; https://doi.org/10.3390/machines13010017 - 30 Dec 2024
Viewed by 196
Abstract
Accurately and quickly estimating the peak pavement adhesion coefficient is crucial for achieving high-quality driving and for optimizing vehicle stability control strategies. However, it also helps with putting forward higher requirements for vehicle driving states, tire model construction, the speed of the convergence, [...] Read more.
Accurately and quickly estimating the peak pavement adhesion coefficient is crucial for achieving high-quality driving and for optimizing vehicle stability control strategies. However, it also helps with putting forward higher requirements for vehicle driving states, tire model construction, the speed of the convergence, and the precision of the estimation algorithm. This paper unequivocally presents two highly effective methods for accurately estimating the peak pavement adhesion coefficient. Firstly, a new dimensionless tire model is constructed. A relationship between the mechanical tire characteristics and peak adhesion coefficient is established by using the Burckhardt model’s analogy between the adhesion coefficient and peak adhesion coefficient, and the UKE algorithm completes the estimation. Secondly, an adaptive variable universe fuzzy algorithm (AVUFS) is established using the follow-up of the adhesion coefficient between the tire and the road surface. Even if the slip rate is less than 5%, the algorithm can still complete accurate estimations and does not depend on the initial given information. Finally, using the estimation advantages of the two algorithms, fusion optimization is performed, and the best estimation result is obtained. Based on the simulation results, the algorithm can quickly and precisely predict the maximum pavement adhesion coefficient in situations where the pavement has a low or high adhesion coefficient. Full article
(This article belongs to the Special Issue Intelligent Control and Active Safety Techniques for Road Vehicles)
Show Figures

Figure 1

Figure 1
<p>The vehicle dynamics model.</p>
Full article ">Figure 2
<p>Typical road adhesion coefficient curves.</p>
Full article ">Figure 3
<p>Identification algorithm diagram.</p>
Full article ">Figure 4
<p>Road identification results: (<b>a</b>) Dry cement prediction results. (<b>b</b>) Wet bituminous prediction results. (<b>c</b>) Wet pebble prediction results. (<b>d</b>) Snow road prediction results.</p>
Full article ">Figure 5
<p>Tire force comparison results: (<b>a</b>) Longitudinal force of left front wheel (<b>b</b>) Left front wheel lateral force. (<b>c</b>) Longitudinal force of right front wheel. (<b>d</b>) Right front wheel lateral force.</p>
Full article ">Figure 6
<p>UKF process chart.</p>
Full article ">Figure 7
<p>Road peak adhesion coefficient estimation flow chart.</p>
Full article ">Figure 8
<p>Interval division diagram.</p>
Full article ">Figure 9
<p>The characteristic curves of the typical pavements.</p>
Full article ">Figure 10
<p>Fuzzy logic observer.</p>
Full article ">Figure 11
<p>Membership function diagram.</p>
Full article ">Figure 12
<p>The utilization adhesion coefficient membership function: (<b>a</b>) Small slip-rate-adhesion characteristics. (<b>b</b>) Large slip-rate-adhesion coefficient.</p>
Full article ">Figure 13
<p>Peak adhesion coefficient membership function diagram.</p>
Full article ">Figure 14
<p>Adhesion coefficient membership function.</p>
Full article ">Figure 15
<p>Estimation of the Fuzzy Adhesion Coefficient in the Variable Universe for Particle Swarm Optimization.</p>
Full article ">Figure 16
<p>Identification results of the AVUSF algorithm.</p>
Full article ">Figure 17
<p>Simulation results under high-speed conditions. (<b>a</b>) Adhesion Coefficient Estimation Results. (<b>b</b>) Slip Ratio Results. (<b>c</b>) Comparison Results of Tire Longitudinal Force. (<b>d</b>) Vehicle Speed.</p>
Full article ">Figure 18
<p>Simulation Results Under Low-Speed Conditions. (<b>a</b>) Adhesion Coefficient Estimation Results. (<b>b</b>) Comparison Results of Tire Longitudinal Force.</p>
Full article ">Figure 19
<p>Adhesion Coefficient Estimation Results With AVUFS: (<b>a</b>) Estimation Results for High-Speed Conditions. (<b>b</b>) Estimation Results for Low-Speed Conditions.</p>
Full article ">Figure 20
<p>Adhesion Coefficient Estimation Results with Fusion Strategy: (<b>a</b>) Estimation Results for High-Speed Conditions. (<b>b</b>) Estimation Results for Low-Speed Conditions.</p>
Full article ">
16 pages, 3040 KiB  
Article
Sensory Feedback of Grasp Security by Direct Neural Stimulation Improves Amputee Prediction of Object Slip
by Andrew B. Smiles, Eric J. Earley, Ning Jiang and Max Ortiz-Catalan
Prosthesis 2025, 7(1), 3; https://doi.org/10.3390/prosthesis7010003 - 30 Dec 2024
Viewed by 322
Abstract
Background: Prostheses are becoming more advanced and biomimetic with time, providing additional capabilities to their users. However, prosthetic sensation lags far behind its natural limb counterpart, limiting the use of sensory feedback in prosthetic motion planning and execution. Without actionable sensation, prostheses may [...] Read more.
Background: Prostheses are becoming more advanced and biomimetic with time, providing additional capabilities to their users. However, prosthetic sensation lags far behind its natural limb counterpart, limiting the use of sensory feedback in prosthetic motion planning and execution. Without actionable sensation, prostheses may never meet the functional requirements to match biological performance. Methods: We propose an approach for upper limb prosthetic grasp security feedback, delivered to the wearer through direct nerve stimulation proportional to the likelihood of objects slipping from grasp. This proportional feedback is based on a linear regression of the sensors embedded in a prosthetic hand to predict slip before it occurs. Four participants with transhumeral amputation performed pulling tasks with their prosthetic hand grasping an object at predetermined grip forces, attempting to pull the object with as much force as possible without slip. These trials were performed with two different prediction notification paradigms. Results: At lower grasp forces, where slip was more likely, a strong, single impulse notification of impending slip reduced the incidence of object slip by a median of 32%, but the maximum achieved pull forces did not change. At higher grasp forces, where slip was less likely, the maximum achieved pull forces increased by a median of 19% across participants when provided with a stimulation strength inversely proportional to the grasp security, but slip incidence was unchanged. Conclusions: These results suggest that this approach may be effective in recreating a lost sense of grip stability in the missing limb that can be incorporated into motor planning and ultimately prevent unanticipated object slips. Full article
Show Figures

Figure 1

Figure 1
<p>The Ottobock SensorHand Speed system (left) includes sensors measuring normal (light red) and shear loads (dark red) at the tip of the thumb, and joint torque (blue) at the thumb joint. These sensors were used to train a slip predictor model, which was incorporated into the Digital Limb Controller (right) as part of this study to provide grasp security sensory feedback.</p>
Full article ">Figure 2
<p>(<b>a</b>) Training block, (<b>b</b>) trial totem detail [mm], and (<b>c</b>) view of trial totem grasped by prosthetic before a pull attempt.</p>
Full article ">Figure 3
<p>Visual example of relation between normal (<span class="html-italic">y</span>) and shear (<span class="html-italic">z</span>) sensor measurements from prosthetic fingertips and regressor output across grasp and pull movements. (<b>a</b>) Grasping object, (<b>b</b>) neutral grasp, (<b>c</b>) pulling object to right until slip, (<b>d</b>) returning to neutral grasp, (<b>e</b>) pulling object to left until slip, (<b>f</b>) returning to neutral grasp.</p>
Full article ">Figure 4
<p>The experimental setup (above) involved one experimenter connecting the trial totem to different elastic bands to ensure that the participant used their sense of pull force, and not pull distance, during trials. A second experimenter recorded the maximum pull force for each trial. The opaque divider (below) blinded the participant to which elastic was in use and the force results from each trial.</p>
Full article ">Figure 5
<p>Median number of objects that slipped from lower-force grasp (15 N) when participants received <span class="html-italic">spike</span> or <span class="html-italic">amplitude stimulation</span> was reduced by 7.5 and 4.5, respectively, compared to <span class="html-italic">no stimulation</span>. Number of slips generally did not change discernably with higher-force grasp (25N).</p>
Full article ">Figure 6
<p>When pulling objects with a higher-force grasp (25 N), participants were able to impart greater pulling forces with <span class="html-italic">spike</span> and <span class="html-italic">amplitude stimulation</span> compared to <span class="html-italic">no feedback</span>. Only <span class="html-italic">spike stimulation</span> resulted in greater pull forces with a lower-force grasp (15 N). Points represent raw data, boxes represent median and quartiles, and whiskers extend to points within 1.5x the interquartile range.</p>
Full article ">Figure 7
<p>Pull forces were generally higher for high-force grasps (25 N) compared to low-force grasps (15 N), as expected. However, differences in median pull forces were larger when participants received <span class="html-italic">spike</span> or <span class="html-italic">amplitude stimulation</span>, indicating greater understanding of grasp security. Points represent raw data, boxes represent median and quartiles, and whiskers extend to points within 1.5x the interquartile range.</p>
Full article ">
19 pages, 18132 KiB  
Article
Notch Fatigue Damage Evolution Mechanism of TC21 Alloy with Multilevel Lamellar Microstructures
by Xiaosong Zhou, Xiang Li, Chaowen Huang, Quan Wu and Fei Zhao
Metals 2025, 15(1), 18; https://doi.org/10.3390/met15010018 - 29 Dec 2024
Viewed by 279
Abstract
This study aims to explore the effect of microstructural parameters on the notch fatigue damage behavior of the TC21 alloy. Different levels of lamellar microstructures were achieved through distinct aging temperatures of 550 °C, 600 °C, and 650 °C. The findings reveal that [...] Read more.
This study aims to explore the effect of microstructural parameters on the notch fatigue damage behavior of the TC21 alloy. Different levels of lamellar microstructures were achieved through distinct aging temperatures of 550 °C, 600 °C, and 650 °C. The findings reveal that increasing aging temperature primarily contributes to the augmentation of α colony (αc) thickness, grain boundaries α phase (GBα) thickness, and α fine (αfine) size alongside a reduction in α lath (αlath) thickness and αfine content. The notch alters stress distribution and relaxation effects at the root, enhancing notched tensile strength while weakening plasticity. Moreover, the increased thickness of GBα emerges as a critical factor leading to the increase area of intergranular cleavage fracture. It is noteworthy that more thickness αlath and smaller αfine facilitate deformation coordination and enhance dislocation accumulation at the interface, leading to a higher propensity for micro-voids and micro-cracks to propagate along the interface. Conversely, at elevated aging temperatures, thinner αlath and larger αfine are more susceptible to fracture, resulting in the liberation of dislocations at the interface. The reduction in αlath thickness is crucial for triggering the initiation of multi-system dislocations at the interface, which promotes the development of persistent slip bands (PSBs) and dislocation nets within αlath. This phenomenon induces inhomogeneous plastic deformation and localized hardening, fostering the formation of micro-voids and micro-cracks. Full article
(This article belongs to the Special Issue Structure and Mechanical Properties of Titanium Alloys)
Show Figures

Figure 1

Figure 1
<p>Original microstructure of TC21 alloy (<b>a</b>) SEM image and (<b>b</b>) TEM image.</p>
Full article ">Figure 2
<p>(<b>a</b>) Geometry of notch tensile and high cycle fatigue specimen, where A and B are represented as two reference symbols (Reprinted from Ref. [<a href="#B14-metals-15-00018" class="html-bibr">14</a>]) (<b>b</b>) 3D model images; (<b>c</b>) real sample.</p>
Full article ">Figure 3
<p>Schematic illustration for (<b>a</b>) SEM observation of micro-voids, micro-cracks and deformation characteristics and (<b>b</b>) TEM observation of microstructural features below the primary fatigue crack initiation site.</p>
Full article ">Figure 4
<p>Microstructure of TC21 alloy after 1010 °C/0.5 h solid solution, 800 °C/2 h/AC annealing and different temperatures: (<b>a</b>,<b>d</b>,<b>g</b>) 550 °C, (<b>b</b>,<b>e</b>,<b>h</b>) 600 °C, (<b>c</b>,<b>f</b>,<b>i</b>) 650 °C aging for 5 h/AC; (<b>a</b>–<b>f</b>) SEM images; (<b>g</b>–<b>i</b>) TEM images.</p>
Full article ">Figure 5
<p>Notch tensile properties under different aging temperatures of stress–strain curves.</p>
Full article ">Figure 6
<p>Notch tensile fracture surfaces of TC21 alloys at aging temperatures of 550 °C (<b>a</b>–<b>c</b>), 600 °C (<b>d</b>–<b>f</b>) and 650 °C (<b>g</b>–<b>i</b>): (<b>a</b>,<b>d</b>,<b>g</b>) low magnification of fracture, (<b>b</b>,<b>e</b>,<b>h</b>) tearing ridges and secondary crack; (<b>c</b>,<b>f</b>,<b>d</b>) dimples.</p>
Full article ">Figure 7
<p>The micro-voids and micro-cracks characteristics underneath the main crack initiation site of specimens A1 (<b>a</b>–<b>c</b>) and A2 (<b>d</b>–<b>f</b>): (<b>a</b>) micro-voids and micro-cracks initiated at the torsional deformed α colony; (<b>b</b>) micro-voids and micro-cracks pileups at α<sub>lath</sub>/β<sub>trans</sub> interface and within the β<sub>trans</sub>; (<b>c</b>) micro-voids nucleated at α<sub>fine</sub> plates; (<b>d</b>) micro-voids and micro-cracks initiated at the α colony at notch root; (<b>e</b>) micro-voids and micro-cracks nucleated at α<sub>lath</sub>/β<sub>trans</sub> interface and along the interfaces; (<b>f</b>) micro-cracks nucleated at the α<sub>lath</sub> and within the torsional deformed α<sub>fine</sub>.</p>
Full article ">Figure 8
<p>The micro-voids and micro-cracks characteristics underneath the main crack initiation site of specimens B1 (<b>a</b>–<b>c</b>) and B2 (<b>d</b>–<b>f</b>): (<b>a</b>) micro-voids and micro-cracks initiated at the torsional deformed α colony; (<b>b</b>) micro-voids and secondary cracks formed at α<sub>lath</sub>/β<sub>trans</sub> interface and GBα; (<b>c</b>) micro-cracks nucleated at the GBα; (<b>d</b>) micro-voids and micro-cracks initiated at the α colony at notch root; (<b>e</b>) micro-voids and micro-cracks nucleated at α<sub>lath</sub>/β<sub>trans</sub> interface and α<sub>fine</sub>/β<sub>r</sub> interface; (<b>f</b>) micro-cracks nucleated at the α<sub>lath</sub> and within the torsional deformed β<sub>r</sub>.</p>
Full article ">Figure 9
<p>The micro-voids and micro-cracks characteristics underneath the main crack initiation site of specimens C1 (<b>a</b>–<b>c</b>) and C2 (<b>d</b>–<b>f</b>): (<b>a</b>) micro-voids and micro-cracks initiated at the torsional deformed α colonies; (<b>b</b>) torsional deformed α colony; (<b>c</b>) micro-voids nucleated at α laths; (<b>d</b>) micro-voids and micro-cracks initiated at the deformed α colony at notch root; (<b>e</b>) micro-voids and micro-cracks nucleated at α<sub>lath</sub>/β<sub>trans</sub> interface and α<sub>fine</sub>/β<sub>r</sub> interface; (<b>f</b>) micro-cracks and slip lines nucleated within the α<sub>fine</sub> and β<sub>r</sub>.</p>
Full article ">Figure 10
<p>The TEM images of fatigue crack initiation region of the interrupted specimen A1(σ = 240 MPa, N = 4 × 10<sup>6</sup> cycles) and A2 (σ = 240 MPa, N = 8 × 10<sup>6</sup> cycles): (<b>A1-a–A1-c</b>) high-density dislocations formed in the α<sub>fine</sub>/β<sub>trans</sub> interface; (<b>A1-d–A1-h</b>) the high-resolution transmission electron diffraction (SAED), fast Fourier transform (FFT) patterns and atoms spacing of (d); (<b>A1-i–A1-k</b>) geometric phase analysis (GPA) of (<b>A1</b>-<b>d</b>); (<b>A2</b>-<b>a,A2</b>-<b>b</b>) high-density dislocations formed in the α<sub>fine</sub>/β<sub>trans</sub> interface; (<b>A2</b>-<b>c</b>) ladder-like structures formed in the α<sub>lath</sub>/β<sub>trans</sub> interface; (<b>A2-d–A2-f</b>) twins formed and SAED in the α<sub>fine</sub>; (<b>A2-g–A2-i</b>) the GPA of (<b>A2</b>-<b>d</b>).</p>
Full article ">Figure 11
<p>The TEM images of fatigue crack initiation region of the interrupted specimen B1 (σ = 280 MPa, N = 4 × 10<sup>6</sup> cycles) and B2 (σ = 280 MPa, N = 8 × 10<sup>6</sup> cycles): (<b>B1-a</b>–<b>B1-c</b>) slip lines and ladder-like structure formed in the α<sub>lath</sub>/β<sub>trans</sub> interface; (<b>B1-d</b>) deformed α<sub>fine</sub> and dislocation tangles formed in the α<sub>fine</sub>/β<sub>trans</sub> interface; (<b>B1-e</b>,<b>B1-f</b>) the SAED and FFT) patterns of (<b>B1-d</b>); (<b>B1-g</b>–<b>B1-i</b>) GPA of (<b>B1-d</b>); (<b>B2-a</b>,<b>B2-b</b>) persistent slip bands (PSBs) and dislocation net formed within the α<sub>lath</sub>; (<b>B2-c</b>) zigzag structure formed in the α<sub>fine</sub>; (<b>B2-d</b>–<b>B2-f</b>) the SAED and FFT in the PSBs; (<b>B2-g</b>–<b>B2-i</b>) the GPA of (<b>B2-d</b>).</p>
Full article ">Figure 12
<p>The TEM images of fatigue crack initiation region of the interrupted specimen C1 (σ =230 MPa, N = 4 × 10<sup>6</sup> cycles) and C2 (σ =230 MPa, N = 8 × 10<sup>6</sup> cycles): (<b>C1</b>-<b>a</b>–<b>C1</b>-<b>c</b>) dislocations tangles and pinning within the α<sub>lath</sub>; (<b>C1-d</b>) zigzag structure formed in the α<sub>fine</sub>; (<b>C1-e</b>) the stacking faults and SAED within the α<sub>fine</sub>; (<b>C1-f</b>) the FFT patterns of (<b>C1-e</b>); (<b>C1-g</b>–<b>C1-i</b>) GPA of (<b>C1-e</b>); (<b>C2</b>-<b>a</b>–<b>C2</b>-<b>c</b>) ladder-like structure and slip lines formed in the α<sub>fine</sub>/β<sub>trans</sub> interface; (<b>C2-d</b>) dislocation walls formed within the α<sub>lath</sub>; (<b>C2-e</b>) dislocation lines formed within the α<sub>lath</sub>; (<b>C2-f</b>) deformed α<sub>fine</sub> and dislocation lines formed within the α<sub>lath</sub>.</p>
Full article ">Figure 13
<p>AFM images showing slip steps at aging temperatures 550 °C (<b>a</b>–<b>c</b>) and 650 °C (<b>d</b>–<b>f</b>) within α<sub>lath</sub>: (<b>a</b>,<b>d</b>) 2D AFM images; (<b>b</b>,<b>e</b>) 3D AFM images showing the detail of slip steps formed inner α<sub>lath</sub> and at α<sub>lath</sub>/β<sub>trans</sub> interface; (<b>c</b>,<b>f</b>) the height of slip steps in (<b>a</b>,<b>d</b>).</p>
Full article ">
18 pages, 4081 KiB  
Article
Study on Influence of Mechanical Behavior of AZ31 Magnesium Alloy Based on GTN Damage Modeling
by Peijie Wang, Chuanchuan Ma, Chun Xue and Zhibing Chu
Materials 2025, 18(1), 90; https://doi.org/10.3390/ma18010090 - 29 Dec 2024
Viewed by 471
Abstract
Damage mechanisms are a key factor in materials science and are essential for understanding and predicting the behavior of materials under complex loading conditions. In this paper, the influence of different directions, different rates and different model parameters on the mechanical behavior of [...] Read more.
Damage mechanisms are a key factor in materials science and are essential for understanding and predicting the behavior of materials under complex loading conditions. In this paper, the influence of different directions, different rates and different model parameters on the mechanical behavior of AZ31 magnesium alloy during the tensile process is investigated based on the secondary development of the VUMAT user subroutine based on the GTN damage model and verified by the tensile experiments at different loading rates and in different directions. The results show that AZ31 magnesium alloy exhibits significant differences in mechanical properties in radial and axial stretching, where the yield strength is lower in the radial direction than in the axial direction, and the elongation is the opposite. Moreover, the maximum stress and elongation of the material decreased with the increasing tensile rate, revealing the importance of the loading rate on the material properties. Compared with the existing studies, this paper determines the GTN model parameters of the AZ31 magnesium alloy extruded state bar by theresponse surface method combined with the optimization algorithm and obtains the parameter set that can accurately describe the damage behavior of this material. The study also found that the nucleation-averaged plastic strain (εN) has the most significant effect on the maximum stress and fracture point of the stress–strain curve by the sensitivity analysis of six key parameters of the GTN model, while the other parameters change the shape of the curve and the local features to different degrees. Further analysis shows that the differences in yield strength and elongation can be attributed to the differences in basal slip, twinning behavior and dynamic recrystallization in the microstructure, which provides an important guidance for the optimization of the microstructure of AZ31 magnesium alloy. This study not only reveals the influence law of loading conditions on the mechanical properties of AZ31 magnesium alloy but also provides a theoretical basis and reference for understanding the damage mechanism of magnesium alloy and optimizing its mechanical properties. Full article
Show Figures

Figure 1

Figure 1
<p>Schematic diagram of void expansion.</p>
Full article ">Figure 2
<p>Schematic diagram of VUMAT subroutine flow.</p>
Full article ">Figure 3
<p>Schematic diagram of materials and specimens: (<b>a</b>) specimen orientation; (<b>b</b>) specimen dimensions.</p>
Full article ">Figure 4
<p>Schematic diagram of grid division.</p>
Full article ">Figure 5
<p>Stress–strain and porosity–strain curves and corresponding stress and porosity nephograms.</p>
Full article ">Figure 6
<p>Simulation of tensile specimen fracture critical point and different fracture pattern nephograms.</p>
Full article ">Figure 7
<p>Experimental tensile specimens with different fracture profiles.</p>
Full article ">Figure 8
<p>Axial and radial experimental and simulated stress–strain curves.</p>
Full article ">Figure 9
<p>Experimental and simulated stress–strain curves for different rates in axial direction.</p>
Full article ">Figure 10
<p>Simulation stress–strain curves under various parameters: (<b>a</b>) the influence of <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> </mrow> </semantics></math> on the simulation curve; (<b>b</b>) the influence of <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>n</mi> </mrow> </msub> </mrow> </semantics></math> on the simulation curve; (<b>c</b>) the influence of <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>c</mi> </mrow> </msub> </mrow> </semantics></math> on the simulation curve; (<b>d</b>) the influence of <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>f</mi> </mrow> </msub> </mrow> </semantics></math> on the simulation curve; (<b>e</b>) the influence of <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ε</mi> </mrow> <mrow> <mi>N</mi> </mrow> </msub> </mrow> </semantics></math> on the simulation curve; (<b>f</b>) the influence of <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>s</mi> </mrow> <mrow> <mi>N</mi> </mrow> </msub> </mrow> </semantics></math> on the simulation curve.</p>
Full article ">
15 pages, 3280 KiB  
Article
Deep Penetration of Shear Deformation in Ferritic Stainless Steel via Differential Speed Rolling Considering Contact Condition
by Siti Fatimah, Warda Bahanan, Jee-Hyun Kang, I Putu Widiantara and Young Gun Ko
Appl. Sci. 2025, 15(1), 155; https://doi.org/10.3390/app15010155 - 27 Dec 2024
Viewed by 479
Abstract
In order to effectively process crystal-structured materials like metal, knowledge of the working slip system during plastic deformation is necessary. Rolling is a widely utilized industrial processing method, and understanding its inherent characteristics can optimize the process and help achieve the desired microstructure [...] Read more.
In order to effectively process crystal-structured materials like metal, knowledge of the working slip system during plastic deformation is necessary. Rolling is a widely utilized industrial processing method, and understanding its inherent characteristics can optimize the process and help achieve the desired microstructure and texture. One key aspect worth investigating is how shear deformation penetrates through the material thickness, particularly in relation to contact conditions. Analyzing slip system activity provides valuable insights into the deep penetration of shear deformation. This is achieved by examining orientation gradients derived from inverse pole figure maps obtained through electron backscatter diffraction. The rotation axis is extracted and compared with that obtained from calculation using simple first-order self-consistent formulation. The analysis was carried out on grains with 001<11¯0>, 001<1¯1¯0>, 111<11¯0>, 111<12¯1>, 111<01¯1>, and 111<1¯1¯2> to see the activity of slip systems of 112<111> when plane strain or plane + shear mode is in operation. The rotation axis from the experiment is in agreement with that from the calculation, which confirmed the activity of the well-known 112<111> slip systems. It was found that 112<111> was active in solo in grain with {111}//ND orientation along the γ-fiber during the early stage of differential speed rolling (DSR). Furthermore, it was revealed that the 112<111> slip system was found active when shear deformation mode was in operation at the center of the sheet, which can only be found in the case of a sample with no lubrication. Conclusion: The current study shows that deep penetration was achieved under contact conditions where no lubrication was used during DSR by revealing the activity of the 112<111> slip system under the shear mode of deformation. Full article
(This article belongs to the Section Chemical and Molecular Sciences)
Show Figures

Figure 1

Figure 1
<p>Schematic illustration of differential speed rolling for the case of sample with lubricant and with no lubricant. The sample’s reference system of the rolled sample are shown.</p>
Full article ">Figure 2
<p>Orientation rotations of the EBSD data were carried out in order to match the global orientation. This particularly important, especially for assessment using an ODF map.</p>
Full article ">Figure 3
<p>Pixel arrangement for orientation gradient analysis. The selected pixels have a minimum of 0.5 confidence index.</p>
Full article ">Figure 4
<p>Schematic illustration of suggested method for single {112}&lt;111&gt; slip system activity.</p>
Full article ">Figure 5
<p>IPF maps imposed with grain boundary maps and {111} PF maps of (<b>a</b>) lubricated and (<b>b</b>) non-lubricated sample.</p>
Full article ">Figure 6
<p>ODF maps (φ1 (0 to 90°), Φ (0 to 90°), and a constant φ2 of 45°) of (<b>a</b>) lubricated and (<b>b</b>) non-lubricated sample. The highlighted textures are those commonly found in a metal sheet after rolling deformation.</p>
Full article ">Figure 7
<p>Three representative datasets providing an overview of the current method. Both experimental and theoretical rotation axes demonstrate the activation of the {112}&lt;111&gt; slip system under plane strain and shear conditions.</p>
Full article ">Figure 8
<p>Statistic for the fraction (orange bar), fraction of grain with active <math display="inline"><semantics> <mrow> <mfenced open="{" close="}" separators="|"> <mrow> <mn>112</mn> </mrow> </mfenced> <mo>&lt;</mo> <mn>111</mn> <mo>&gt;</mo> </mrow> </semantics></math> aligned with calculated plane strain mode (green bar), and fraction of grain with active <math display="inline"><semantics> <mrow> <mfenced open="{" close="}" separators="|"> <mrow> <mn>112</mn> </mrow> </mfenced> <mo>&lt;</mo> <mn>111</mn> <mo>&gt;</mo> </mrow> </semantics></math> aligned with calculated plane strain and shear mode (blue bar) of grain with (<b>a</b>) <math display="inline"><semantics> <mrow> <mfenced open="{" close="}" separators="|"> <mrow> <mn>001</mn> </mrow> </mfenced> <mo>&lt;</mo> <mn>1</mn> <mover accent="true"> <mrow> <mn>1</mn> </mrow> <mo stretchy="false">¯</mo> </mover> <mn>0</mn> <mo>&gt;</mo> </mrow> </semantics></math>, (<b>b</b>) <math display="inline"><semantics> <mrow> <mfenced open="{" close="}" separators="|"> <mrow> <mn>001</mn> </mrow> </mfenced> <mo>&lt;</mo> <mover accent="true"> <mrow> <mn>1</mn> </mrow> <mo stretchy="false">¯</mo> </mover> <mover accent="true"> <mrow> <mn>1</mn> </mrow> <mo stretchy="false">¯</mo> </mover> <mn>0</mn> <mo>&gt;</mo> </mrow> </semantics></math>, (<b>c</b>) <math display="inline"><semantics> <mrow> <mfenced open="{" close="}" separators="|"> <mrow> <mn>111</mn> </mrow> </mfenced> <mo>&lt;</mo> <mn>1</mn> <mover accent="true"> <mrow> <mn>1</mn> </mrow> <mo stretchy="false">¯</mo> </mover> <mn>0</mn> <mo>&gt;</mo> </mrow> </semantics></math>, (<b>d</b>) <math display="inline"><semantics> <mrow> <mfenced open="{" close="}" separators="|"> <mrow> <mn>111</mn> </mrow> </mfenced> <mo>&lt;</mo> <mn>1</mn> <mover accent="true"> <mrow> <mn>2</mn> </mrow> <mo stretchy="false">¯</mo> </mover> <mn>1</mn> <mo>&gt;</mo> </mrow> </semantics></math>, (<b>e</b>)<math display="inline"><semantics> <mrow> <mo> </mo> <mfenced open="{" close="}" separators="|"> <mrow> <mn>111</mn> </mrow> </mfenced> <mo>&lt;</mo> <mn>0</mn> <mover accent="true"> <mrow> <mn>1</mn> </mrow> <mo stretchy="false">¯</mo> </mover> <mn>1</mn> <mo>&gt;</mo> </mrow> </semantics></math>, (<b>f</b>) <math display="inline"><semantics> <mrow> <mfenced open="{" close="}" separators="|"> <mrow> <mn>111</mn> </mrow> </mfenced> <mo>&lt;</mo> <mover accent="true"> <mrow> <mn>1</mn> </mrow> <mo stretchy="false">¯</mo> </mover> <mover accent="true"> <mrow> <mn>1</mn> </mrow> <mo stretchy="false">¯</mo> </mover> <mn>2</mn> <mo>&gt;</mo> <mo>,</mo> </mrow> </semantics></math> and (<b>g</b>) other orientations. The letters a, ab, b, bc, and c are added to summarize the results of the ANOVA.</p>
Full article ">
20 pages, 9663 KiB  
Article
Research on the Failure Mechanism and Treatment Technology of Landslides in Typical Accumulation Bodies Along Highways in Qinghai Province
by Yunfei Yang, Zixuan Yang, Wanzhong Xu, Fayou A, Yinghang Guo and Jieru Zheng
Water 2025, 17(1), 34; https://doi.org/10.3390/w17010034 - 26 Dec 2024
Viewed by 349
Abstract
Landslides on the Jiaxi Highway in Qinghai Province threaten construction safety and quality. The on-site data analysis shows that excavation at the foot of the slope and heavy rainfall are the key factors causing the displacement of the Q1 monitoring point by 1825 [...] Read more.
Landslides on the Jiaxi Highway in Qinghai Province threaten construction safety and quality. The on-site data analysis shows that excavation at the foot of the slope and heavy rainfall are the key factors causing the displacement of the Q1 monitoring point by 1825 mm. This article uses numerical simulation methods combined with the strength reduction method to study the stability changes of slopes under different working conditions. Numerical simulations identified the landslide location and predicted a 1960 mm slip and a safety factor of 1.26 under natural conditions, indicating risks. The study adopted a strategy combining slope cutting, load reduction, and sheet pile wall reinforcement. After the first treatment, the safety factor rose to 1.83 with a 40 mm displacement; after the second, it reached 2.36 with a 37 mm displacement. Continuous monitoring showed a 50 mm displacement over six months, indicating stability. Rainfall simulations before and after treatment explained the stability evolution and local slope stability. Treatments increased the safety factor to 2.16 with a 17.6 mm displacement. This study significantly improved highway landslide stability and verified treatment effectiveness, providing a reference for similar geological conditions. Full article
Show Figures

Figure 1

Figure 1
<p>Geographic location of the study area.</p>
Full article ">Figure 2
<p>Borehole information for the study area. (<b>a</b>) Upper Triassic Nanying’er Formation sandstone; (<b>b</b>) Quaternary Holocene floodplain sand pebbles.</p>
Full article ">Figure 3
<p>Slope displacement monitoring points.</p>
Full article ">Figure 4
<p>Slope displacement monitoring data.</p>
Full article ">Figure 5
<p>Panoramic image of the landslide.</p>
Full article ">Figure 6
<p>H1 landslide boundary.</p>
Full article ">Figure 7
<p>Geological profile of section 1-1′.</p>
Full article ">Figure 8
<p>Numerical simulation model diagram.</p>
Full article ">Figure 9
<p>Displacement and plastic zone variations under natural working conditions: (<b>a</b>) x-displacement; (<b>b</b>) plastic zone.</p>
Full article ">Figure 10
<p>First cut slope + support.</p>
Full article ">Figure 11
<p>Effectiveness of governance: (<b>a</b>) x-displacement; (<b>b</b>) plastic zone.</p>
Full article ">Figure 12
<p>Second slope cutting + support.</p>
Full article ">Figure 13
<p>Effectiveness of governance: (<b>a</b>) x-displacement; (<b>b</b>) plastic zone.</p>
Full article ">Figure 14
<p>Post-disposal displacement monitoring data.</p>
Full article ">Figure 15
<p>Pore water pressure.</p>
Full article ">Figure 16
<p>Variation of safety factor with seepage time.</p>
Full article ">Figure 17
<p>Slope displacement monitoring: (<b>a</b>) monitoring point 1; (<b>b</b>) monitoring point 2.</p>
Full article ">Figure 18
<p>Variation of pore water pressure in slope: (<b>a</b>) monitoring point 1; (<b>b</b>) monitoring point 2.</p>
Full article ">Figure 19
<p>Pore water pressure (A1, A2 and A3 are slope displacement monitoring points).</p>
Full article ">Figure 20
<p>Slope displacement monitoring.</p>
Full article ">
27 pages, 11214 KiB  
Article
Fractal Characteristics of the Spatial Distribution of Mine Earthquake Sources in the Vicinity of a Fault: A Case Study in the Ashele Copper Mine
by Congcong Zhao, Shigen Fu and Yinghua Huang
Fractal Fract. 2025, 9(1), 3; https://doi.org/10.3390/fractalfract9010003 - 24 Dec 2024
Viewed by 291
Abstract
Potential faults are common sensitive geological bodies that affect the safe mining of underground mines, often leading to major accidents such as rock instability and rockburst during mining. The failure mechanism of faults has been widely studied. However, due to the spatiotemporal specificity [...] Read more.
Potential faults are common sensitive geological bodies that affect the safe mining of underground mines, often leading to major accidents such as rock instability and rockburst during mining. The failure mechanism of faults has been widely studied. However, due to the spatiotemporal specificity of fault occurrence, there are few theoretical and mathematical methods suitable for effective analysis in mine safety risk management. This study aims to introduce fractal theory to characterize the spatiotemporal activity fractal characteristics of induced faults intersecting the mining site and roadway during the mining process of the Ashele copper mine in China. Using microseismic systems and fractal theory, a spatiotemporal fractal model of the fault slip process is constructed, and a fractal analysis method is proposed. The fractal dimension value is calculated based on the spatiotemporal parameters of different segments and stages. The fractal dimension is used to characterize and analyze the evolution of the fault. The physical formation process of potential faults and the relationship between fractal dimension values and multiple parameters, including spatial clustering, regional distribution characteristics, and energy-release characteristics, were analyzed based on the division of events into different time stages. Discovering fractal dimension’s temporal and spatial–temporal characteristics can provide technical references for mine disaster prevention. Full article
(This article belongs to the Special Issue Fractal Analysis and Its Applications in Rock Engineering)
Show Figures

Figure 1

Figure 1
<p>The mine location, landform, microseismic monitoring topology system, and underground system. (<b>a</b>) geographical location; (<b>b</b>) topographic features; (<b>c</b>) development Engineering and Microseismic Monitoring; (<b>d</b>) topological structure.</p>
Full article ">Figure 2
<p>The layout of the target area and monitoring network: (<b>a</b>) stereo diagram; (<b>b</b>) top plan view.</p>
Full article ">Figure 3
<p>The relationships between the positions of the microseismic monitoring sensors and the middle levels in the study area. (<b>a</b>) +450m middle and its microseismic events.; (<b>b</b>) +350m middle and its microseismic events.; (<b>c</b>) +300m middle and its microseismic events.</p>
Full article ">Figure 4
<p>A flow diagram of the research method and fractal dimension analysis.</p>
Full article ">Figure 5
<p>The frequency distribution sand stage divisions of daily microseismic activities: (<b>a</b>) overall mine events; and (<b>b</b>) the distribution of microseismic events near mining-induced faults.</p>
Full article ">Figure 6
<p>The distribution and location relationships of microseismic events in the four different stages. (<b>a</b>) overall situation; (<b>b</b>) Localized enlargement.</p>
Full article ">Figure 7
<p>A 3D spatial fractal dimension representation frame model, based on the locations of the mine’s earthquake sources. (<b>a</b>) Time scale division; (<b>b</b>) The nesting process of events and spatial units; (<b>c</b>) Nesting results of events and spatial units.</p>
Full article ">Figure 8
<p>The distributions of the microseismic events around mining-induced faults in the four time stages.</p>
Full article ">Figure 9
<p>A comparison of the fitting coefficients of the maximum events and fractal dimension values in microcells using different grids.</p>
Full article ">Figure 10
<p>The fractal dimension distributions.</p>
Full article ">Figure 11
<p>A perspective cloud chart of the fractal dimension interpolation under different perspectives in each time stage.</p>
Full article ">Figure 12
<p>A schematic diagram of the fractal dimension value distributions in overall space in the different time stages.</p>
Full article ">Figure 13
<p>A contour map of the middle-level fractal dimension interpolation in the different time stages.</p>
Full article ">Figure 14
<p>A distribution diagram of the fractal dimension values in the middle levels of the different time stages.</p>
Full article ">Figure 15
<p>A comparison chart of the fractal dimension values and the number of events in the middle level of each time stage. (<b>a</b>) Changes in fractal dimension at different stages; (<b>b</b>) Changes in the number of events at different stages.</p>
Full article ">Figure 16
<p>A comparison diagram of the changes in the main parameter of the microseismic events. (<b>a</b>) radiant energy; (<b>b</b>) richter magnitude; (<b>c</b>) seismic moment; (<b>d</b>) source radius.</p>
Full article ">
13 pages, 8877 KiB  
Article
The Influence of the Strain Rate on Texture Formation During the Plane Strain Compression of AZ80 Magnesium Alloy
by Yebeen Ji, Jimin Yun, Kibeom Kim, Tae Hee Lee and Kwonhoo Kim
Materials 2024, 17(24), 6292; https://doi.org/10.3390/ma17246292 - 23 Dec 2024
Viewed by 252
Abstract
Controlling microstructure and texture development is a key approach to improving the formability of magnesium alloys. In this study, the effects of the strain rate and initial texture on the texture evolution of magnesium alloys during high-temperature processing are investigated. The plane strain [...] Read more.
Controlling microstructure and texture development is a key approach to improving the formability of magnesium alloys. In this study, the effects of the strain rate and initial texture on the texture evolution of magnesium alloys during high-temperature processing are investigated. The plane strain compression of three types of AZ80 magnesium alloys with different initial textures was assessed at 723 K and a train rate of 0.0005 s−1. Work softening was consistently observed in the stress–strain curves of all samples. However, the peak stress varied depending on the initial texture, with lower peak stress observed under conditions favoring prismatic slip. Under these conditions, the activation of non-basal slip suppressed the formation of basal texture. The texture shifted and developed parallel to the transverse direction when prismatic slip was dominant. In contrast, the activation of pyramidal slip led to the formation of a basal texture tilted by 25° from the (0001) plane. The effects of recrystallization and grain boundary migration on texture development were minimal. This study contributes to understanding the texture development mechanisms in magnesium alloys and provides insights into improving their workability and ductility through texture modification. Full article
(This article belongs to the Special Issue Advances in Materials Processing (3rd Edition))
Show Figures

Figure 1

Figure 1
<p>Schematics of specimens: Type A, Type B, and Type C.</p>
Full article ">Figure 2
<p>Microstructures of specimens after rolling and annealing: (<b>a</b>) Type A, (<b>b</b>) Type B, and (<b>c</b>) Type C.</p>
Full article ">Figure 3
<p>The <math display="inline"><semantics> <mrow> <mo>(</mo> <mn>0001</mn> <mo>)</mo> </mrow> </semantics></math> pole figures of (<b>a</b>) Type A, (<b>b</b>) Type B, and (<b>c</b>) Type C specimens before plane strain compression.</p>
Full article ">Figure 4
<p>True stress–strain curves for deformation at 723 K up to a strain of −1.0 at a strain rate of 0.0005 s<sup>−1</sup>.</p>
Full article ">Figure 5
<p>The <math display="inline"><semantics> <mrow> <mo>(</mo> <mn>0001</mn> <mo>)</mo> </mrow> </semantics></math> pole figures of Type A specimens compressed at 723 K and 0.0005s<sup>−</sup>¹ after true strains of (<b>a</b>) −0.4, (<b>b</b>) −0.7, and (<b>c</b>) −1.0.</p>
Full article ">Figure 6
<p>The <math display="inline"><semantics> <mrow> <mo>(</mo> <mn>0001</mn> <mo>)</mo> </mrow> </semantics></math> pole figures of Type B specimens compressed at 723 K and 0.0005s<sup>−</sup>¹ after true strains of (<b>a</b>) −0.4, (<b>b</b>) −0.7, and (<b>c</b>) −1.0.</p>
Full article ">Figure 7
<p>The <math display="inline"><semantics> <mrow> <mo>(</mo> <mn>0001</mn> <mo>)</mo> </mrow> </semantics></math> pole figures of Type C specimens compressed at 723 K and 0.0005 s <sup>−1</sup> after true strains of (<b>a</b>) −0.4, (<b>b</b>) −0.7, and (<b>c</b>) −1.0.</p>
Full article ">Figure 8
<p>Microstructures of (<b>a</b>) Type A, (<b>b</b>) Type B, and (<b>c</b>) Type C specimens according to EBSD measurements at a strain rate of 0.0005 s<sup>−</sup>¹ after deformation up to a strain of −1.0.</p>
Full article ">Figure 9
<p>The average grain size of each type specimen after plane strain compression from strain 0 to −1.0.</p>
Full article ">Figure 10
<p>(<b>a</b>) GOS and (<b>b</b>) KAM map of the Type A specimen observed after the plane strain compression, with a strain of up to −1.0.</p>
Full article ">Figure 11
<p>(<b>a</b>) A relationship between texture intensities and true strain. Texture components are shown above each point. (<b>b</b>) Microstructure and (<b>c</b>) the <math display="inline"><semantics> <mrow> <mo>(</mo> <mn>0001</mn> <mo>)</mo> </mrow> </semantics></math> pole figure of Type C specimen compressed up to the true strain −1.4.</p>
Full article ">
Back to TopTop