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31 pages, 13872 KiB  
Article
Hyperelastic and Stacked Ensemble-Driven Predictive Modeling of PEMFC Gaskets Under Thermal and Chemical Aging
by Su-Yeon Park, Akeem Bayo Kareem, Toyyeebah Ajibola Mustapha, Woo-Jeong Joo and Jang-Wook Hur
Materials 2024, 17(22), 5675; https://doi.org/10.3390/ma17225675 - 20 Nov 2024
Viewed by 764
Abstract
This study comprehensively investigates the stress distribution and aging effects in Ethylene Propylene Diene Monomer (EPDM) and Liquid Silicone Rubber (LSR) gasket materials through a novel integration of hyperelastic modeling and advanced machine learning techniques. By employing the Mooney–Rivlin, Ogden, and Yeoh hyperelastic [...] Read more.
This study comprehensively investigates the stress distribution and aging effects in Ethylene Propylene Diene Monomer (EPDM) and Liquid Silicone Rubber (LSR) gasket materials through a novel integration of hyperelastic modeling and advanced machine learning techniques. By employing the Mooney–Rivlin, Ogden, and Yeoh hyperelastic models, we evaluated the mechanical behavior of EPDM and LSR under conditions of no aging, heat aging, and combined heat- and sulfuric-acid exposure. Each model revealed distinct sensitivities to stress distribution and material deformation, with peak von Mises stress values indicating that LSR experiences higher internal stress than EPDM across all conditions. For instance, without aging, LSR shows a von Mises stress of 24.17 MPa compared to 14.96 MPa for EPDM, while under heat and sulfuric acid exposure, LSR still exhibits higher stress values, showcasing its resilience under extreme conditions. Additionally, the ensemble learning approach achieved a classification accuracy of 98% for LSR and 84% for EPDM in predicting aging effects, underscoring the robustness of our predictive framework. These findings offer practical implications for selecting suitable gasket materials and developing predictive maintenance strategies in industrial applications, such as fuel cells, where material integrity under stress and aging is paramount. Full article
(This article belongs to the Special Issue Advanced Materials: Process, Properties, and Applications)
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Figure 1
<p>Proposed hyperelastic modeling approach for PEMFC gasket materials.</p>
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<p>Mesh generation using Hypermesh for the gasket material simulation.</p>
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<p>A cross-sectional profile of the gasket assembly, showing the Pi film layer, cathode, and anode sections, and supporting plates for structural stability.</p>
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<p>The framework of the stacking ensemble model.</p>
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<p>Contact-stress contour distribution of <b>EPDM</b> under different aging conditions: (<b>a</b>) no aging (Ogden); (<b>b</b>) heat (Mooney–Rivlin); and (<b>c</b>) heat + sulfuric acid (Yeoh).</p>
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<p>Contact-stress contour distribution of <b>LSR</b> under different aging conditions: (<b>a</b>) no aging (Mooney–Rivlin); (<b>b</b>) heat (Ogden); and (<b>c</b>) heat + sulfuric acid (Yeoh).</p>
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<p>von Mises stress distribution of <b>EPDM</b> under different aging conditions: (<b>a</b>) no aging (Ogden); (<b>b</b>) heat (Mooney–Rivlin); and (<b>c</b>) heat + sulfuric acid (Yeoh).</p>
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<p>von Mises stress distribution of <b>LSR</b> under different aging conditions: (<b>a</b>) no aging (Mooney–Rivlin), (<b>b</b>) heat (Ogden); and (<b>c</b>) heat + sulfuric acid (Yeoh).</p>
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<p>Comparison of classification accuracy for LSR and EPDM materials using RandomSearchCV and GridSearchCV for model type (M) and aging type (A) classification.</p>
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<p>Mooney–Rivlin model analysis of von Mises stress, contact stress, and height (deformation) for LSR materials under no aging conditions.</p>
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<p>Mooney–Rivlin model analysis of von Mises stress, contact stress, and height (deformation) for LSR materials under heat-aging conditions.</p>
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<p>Mooney–Rivlin model analysis of von Mises stress, contact stress, and height (deformation) for LSR materials under heat- + sulfuric-acid-aging conditions.</p>
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<p>Ogden model analysis of von Mises stress, contact stress, and height (deformation) for LSR materials under no aging conditions.</p>
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<p>Ogden model analysis of von Mises stress, contact stress, and height (deformation) for LSR materials under heat-aging conditions.</p>
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<p>Ogden model analysis of von Mises stress, contact stress, and height (deformation) for LSR materials under heat- + sulfuric-acid-aging conditions.</p>
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<p>Yeoh model analysis of von Mises stress, contact stress, and height (deformation) for LSR materials under no aging conditions.</p>
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<p>Yeoh model analysis of von Mises stress, contact stress, and height (deformation) for LSR materials under heat-aging conditions.</p>
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<p>Yeoh model analysis of von Mises stress, contact stress, and height (deformation) for LSR materials under heat- + sulfuric-acid-aging conditions.</p>
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<p>Mooney–Rivlin model analysis of von Mises stress, contact stress, and height (deformation) for EPDM material under no aging conditions.</p>
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<p>Mooney–Rivlin model analysis of von Mises stress, contact stress, and height (deformation) for EPDM material under heat-aging conditions.</p>
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<p>Mooney–Rivlin model analysis of von Mises stress, contact stress, and height (deformation) for EPDM material under heat- + sulfuric-acid-aging conditions.</p>
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<p>Ogden model analysis of von Mises stress, contact stress, and height (deformation) for EPDM material under no aging conditions.</p>
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<p>Ogden model analysis of von Mises stress, contact stress, and height (deformation) for EPDM material under heat-aging conditions.</p>
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<p>Ogden model analysis of von Mises stress, contact stress, and height (deformation) for EPDM material under heat- + sulfuric-acid-aging conditions.</p>
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<p>Yeoh model analysis of von Mises stress, contact stress, and height (deformation) for EPDM material under no aging conditions.</p>
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<p>Yeoh model analysis of von Mises stress, contact stress, and height (deformation) for EPDM material under heat-aging conditions.</p>
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<p>Yeoh model analysis of von Mises stress, contact stress, and height (deformation) for EPDM material under heat- + sulfuric-acid-aging conditions.</p>
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17 pages, 4190 KiB  
Article
From Formulation to Application: Effects of Plasticizer on the Printability of Fluoro Elastomer Compounds and Additive Manufacturing of Specialized Seals
by Mookkan Periyasamy, AA Mubasshir, Stiven Kodra, Sangeetham Chandramouli, Ronald Campbell, David O. Kazmer and Joey L. Mead
Micromachines 2024, 15(5), 622; https://doi.org/10.3390/mi15050622 - 5 May 2024
Cited by 1 | Viewed by 1507
Abstract
This work investigated material extrusion additive manufacturing (MatEx AM) of specialized fluoroelastomer (FKM) compounds for applications in rubber seals and gaskets. The influence of a commercially available perfluoropolyether (PFPE) plasticizer on the printability of a control FKM rubber compound was studied using a [...] Read more.
This work investigated material extrusion additive manufacturing (MatEx AM) of specialized fluoroelastomer (FKM) compounds for applications in rubber seals and gaskets. The influence of a commercially available perfluoropolyether (PFPE) plasticizer on the printability of a control FKM rubber compound was studied using a custom-designed ram material extruder, Additive Ram Material Extruder (ARME), for printing fully compounded thermoset elastomers. The plasticizer’s effectiveness was assessed based on its ability to address challenges such as high compound viscosity and post-print shrinkage, as well as its impact on interlayer adhesion. The addition of the PFPE plasticizer significantly reduced the FKM compound’s viscosity (by 70%) and post-print shrinkage (by 65%). While the addition of the plasticizer decreased the tensile strength of the control compound, specimens printed with the plasticized FKM retained 34% of the tensile strength of compression-molded samples, compared to only 23% for the unplasticized compound. Finally, the feasibility of seals and gaskets manufacturing using both conventional and unconventional additive manufacturing (AM) approaches was explored. A hybrid method combining AM and soft tooling for compression molding emerged as the optimal method for seal and gasket fabrication. Full article
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<p>Three-dimensional model of the Additive Ram Material Extruder-3XL (ARME-3XL) printhead.</p>
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<p>Schematic representation (not to scale) of specimen dimension and print pattern used for post-print shrinkage measurement.</p>
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<p>Compression-molded and three types of printed tensile specimens tested for each rubber compound. Sequentially from left to right: compression-molded, printed: parallel to applied force, printed: normal to applied force, and printed: zigzag (+45°/−45°). All tensile specimens were prepared following the ASTM D412—Type C tensile specimen at half-scale.</p>
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<p>Cure curve of FKM compounds at printing temperature of 100 °C (<b>left</b>) and oven cure temperature of 160 °C (<b>right</b>).</p>
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<p>Correlation between the FKM compound viscosity and post-print shrinkage.</p>
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<p>Tensile properties of compression-molded and printed samples of FKM compounds: (<b>left</b>) ultimate tensile stress and (<b>right</b>) ultimate tensile strain.</p>
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<p>Normalized stress at break, an indication of interlayer adhesion of printed parts.</p>
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<p>Conventional approach to additively manufacture a static seal from FKM rubber compound: (<b>a</b>) adapter seal geometry and dimensions, (<b>b</b>) printed adapter seal, and (<b>c</b>) cross-section of printed adapter seal.</p>
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<p>Traditional and direct additive manufacturing of an adapter seal with help of an enlarged nozzle and thermoplastic support structure: (<b>a</b>) 3D model of seal and thermoplastic support structure; (<b>b</b>) 3D-printed support structure and rubber seal; (<b>c</b>) 3D-printed rubber seal after thermal cure and removal of thermoplastic support structure; (<b>d</b>) cross-section of a 3D-printed FKM seal.</p>
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<p>Soft tooling approach to fabricate seals: (<b>a</b>) deposition of uncured FKM rubber directly in the cavity of 3D-printed thermoplastic mold, (<b>b</b>) formed FKM seal with flash after completion of compression cycle, (<b>c</b>) FKM seal after removal of flash, (<b>d</b>) FKM seal after removal from 3D-printed thermoplastic mold/ soft tool.</p>
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<p>Additive manufacturing of bonded seal directly on seal housing: (<b>a</b>) metal seal housing; (<b>b</b>) deposition of FKM rubber compound directly inside of the seal housing; (<b>c</b>) printed seal after thermal cure (top view); (<b>d</b>) printed seal after thermal cure (right view).</p>
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15 pages, 4899 KiB  
Article
Mitigation of Silicon Contamination in Fuel Cell Gasket Materials through Silica Surface Treatment
by Yoo Lim Sim, Jaewon Lee, Su Min Oh, Dong Beom Kim, Kijong Kim, Sung-Hyeon Baeck, Sang Eun Shim and Yingjie Qian
Polymers 2024, 16(7), 914; https://doi.org/10.3390/polym16070914 - 26 Mar 2024
Cited by 1 | Viewed by 1281
Abstract
Gaskets and seals are essential components in the operation of proton exchange membrane (PEM) fuel cells and are required for keeping hydrogen and air/oxygen within their individual compartments. The durability of these gaskets and seals is necessary, as it influences not only the [...] Read more.
Gaskets and seals are essential components in the operation of proton exchange membrane (PEM) fuel cells and are required for keeping hydrogen and air/oxygen within their individual compartments. The durability of these gaskets and seals is necessary, as it influences not only the lifespan but also the electrochemical efficiency of the PEM fuel cell. In this study, the cause of silicon leaching from silicone gaskets under simulated fuel cell conditions was investigated. Additionally, to reduce silicon leaching, the silica surface was treated with methyltrimethoxysilane, vinyltriethoxysilane, and (3,3,3-trifluoropropyl)trimethoxysilane. Changes in the silica surface chemistry were investigated by scanning electron microscopy, energy dispersive X-ray spectroscopy, thermogravimetric analysis, elemental analysis, X-ray photoelectron spectroscopy, and Fourier transform infrared spectroscopy. Inductively coupled plasma-optical emission spectroscopy analysis revealed that surface-treated silica was highly effective in reducing silicon leaching. Full article
(This article belongs to the Special Issue Polymer-SiO2 Composites II)
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<p>Schematic of the commercial LSR test: (<b>a</b>) LSR containing silica and (<b>b</b>) LSR without silica.</p>
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<p>Schematic of the procedure for preparing surface-modified silica nanoparticles.</p>
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<p>Schematic of the procedure for preparing silicone rubber/silica filler composites.</p>
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<p>SEM microphotographs of the material in the residual solution from the commercial silicone rubber containing silica: (<b>a</b>) low magnification and (<b>b</b>) high magnification.</p>
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<p>SEM micrographs of (<b>a</b>) fumed silica, (<b>b</b>) MVF-SiO<sub>2</sub>-1, (<b>c</b>) MVF-SiO<sub>2</sub>-2, (<b>d</b>) MVF-SiO<sub>2</sub>-4, and (<b>e</b>) MVF-SiO<sub>2</sub>-16.</p>
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<p>TGA thermograms of fumed silica and surface-modified silica.</p>
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<p>XPS analysis of silica before and after surface treatment, the survey spectrum of treated silica samples (<b>a</b>), SiO<sub>2</sub> (<b>b</b>), MVF-SiO<sub>2</sub>-1 (<b>c</b>), MVF-SiO<sub>2</sub>-2 (<b>d</b>), MVF-SiO<sub>2</sub>-4 (<b>e</b>), and MVF-SiO<sub>2</sub>-16 (<b>f</b>).</p>
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<p>FT-IR spectra of silica before and after surface treatment in the range of (<b>a</b>) 3900–2700 cm<sup>−1</sup> and (<b>b</b>) 2000–400 cm<sup>−1</sup>.</p>
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<p>SEM micrographs of (<b>a</b>) silicone rubber/fumed silica, (<b>b</b>) silicone rubber/MVF-SiO<sub>2</sub>-1, (<b>c</b>) silicone rubber/MVF-SiO<sub>2</sub>-2, (<b>d</b>) silicone rubber/ MVF-SiO<sub>2</sub>-4, and (<b>e</b>) silicone rubber/MVF-SiO<sub>2</sub>-16.</p>
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<p>Mechanical properties of silicone rubber/silica filler composites: (<b>a</b>) tensile strength, (<b>b</b>) elongation at break, and (<b>c</b>) hardness.</p>
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20 pages, 10190 KiB  
Article
Improvement of the Cracking Moment-Based Asphalt Mixture Splitting Test Method and Splitting Strength Research
by Hongxin Guan, Wang Pan, Hairong Yang and Yuxuan Yang
Buildings 2024, 14(2), 457; https://doi.org/10.3390/buildings14020457 - 7 Feb 2024
Viewed by 960
Abstract
The asphalt mixture splitting test is one of the most important methods for measuring asphalt’s tensile properties. To characterize the limitations of the traditional splitting test and the influence of the specimen size and loading conditions on the accuracy of the test, the [...] Read more.
The asphalt mixture splitting test is one of the most important methods for measuring asphalt’s tensile properties. To characterize the limitations of the traditional splitting test and the influence of the specimen size and loading conditions on the accuracy of the test, the factors affecting the strength of the splitting test were analyzed to reveal the splitting failure state and establish a unified representation model between the splitting and direct tensile tests. Initially, the moment of specimen cracking was taken as a key indicator, combined with image processing technology, to establish a set of criteria to judge the splitting test. Subsequently, standardized splitting tests were conducted and compared to tests of different specimen sizes and loading methods. Based on the octahedral strength theory, the stress points before and after the improved test were compared to the existing failure criteria. Direct tensile and splitting tests were conducted at different rates, and a unified strength–rate function model was established, realizing the unified representation of direct tensile and splitting tests. The research results indicate that the standardized splitting test is prone to the phenomenon wherein the specimen end face cracks before the center, affecting the accuracy of the test and potentially leading to redundant material strength evaluations. Using a loading method with a “35 mm specimen thickness” and a “0.3 mm rubber gasket + 12.7 mm arc-shaped batten” can essentially achieve the test hypothesis of “cracking at the center first”, resulting in less discrete outcomes and closer alignment to the three-dimensional stress failure state. The tensile and splitting strengths are both power function relationships with the rate as the independent variable, establishing a unified function model of the tensile and failure strengths. The research provides a more reliable testing method and calculation model for asphalt pavement structure design, and it also provides an effective basis for the improvement of splitting tests on materials such as concrete and rock. Full article
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<p>Research plan.</p>
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<p>The specimen fabrication process.</p>
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<p>Example of specimen splitting and loading.</p>
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<p>Distribution of the strain gauges on the specimen.</p>
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<p>Splitting test of test piece 1. (<b>a</b>) Initial stage end stress concentration cracking. (<b>b</b>) The crack starts to expand. (<b>c</b>) The crack extends to the center area. (<b>d</b>) Formation of through cracks.</p>
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<p>Splitting test of test piece 2. (<b>a</b>) Initial stage end stress concentration cracking. (<b>b</b>) Cracking at the center of the circle. (<b>c</b>) Crack propagation stage. (<b>d</b>) Formation of through cracks.</p>
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<p>Time difference and MTS peak load in the specimens of “central cracks first”.</p>
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<p>Time differences for differently sized specimens.</p>
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<p>Starting state of the 19 mm arc bead splitting end face.</p>
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<p>State of the splitting end face of the rigid pressing plate at the time of starting.</p>
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<p>The 19 mm arc bead splitting failure state.</p>
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<p>Splitting failure state of the rigid pressing plate.</p>
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<p>Time difference in various test loading fixtures.</p>
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<p>Principle of rubber gasket splitting test. (<b>a</b>) Initial loading stage of the 12.7 mm arc-shaped batten. (<b>b</b>) Initial loading stage of the rigid pressing plate.</p>
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<p>Scatter plot of the data at the time of cracking.</p>
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<p>Failure time difference between the strain gauge and MTS under different test conditions.</p>
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<p>Stress–strain at the center of a circle with different improvement strategies using rubber gaskets. (<b>a</b>) A 3 mm rubber gasket + rigid pressing plate; (<b>b</b>) 1 mm rubber gasket + rigid pressing plate; (<b>c</b>) 10 mm rubber gasket + 12.7 mm arc-shaped batten; (<b>d</b>) 1 mm rubber gasket + 12.7 mm arc-shaped batten; (<b>e</b>) 0.5 mm rubber gasket + 12.7 mm arc-shaped batten; (<b>f</b>) 0.3 mm rubber gasket + 12.7 mm arc-shaped batten.</p>
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<p>Displacement cloud maps at different time points.</p>
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<p>Damage curves and stress points.</p>
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<p>Tensile test loading process.</p>
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<p>Specimen after loading for the tensile test.</p>
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<p>Strength–rate relationship diagram.</p>
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12 pages, 1902 KiB  
Article
Monte Carlo Computer Simulations of Spin-Transfer Torque
by Sergey V. Belim and Igor V. Bychkov
Materials 2023, 16(20), 6728; https://doi.org/10.3390/ma16206728 - 17 Oct 2023
Cited by 1 | Viewed by 849
Abstract
This article performs computer simulations of the change in magnetization in the ferromagnetic film when polarized electric current passes through it. The model examines multilayer structures from ferromagnetic and nonmagnetic films. A sandwich system comprises two ferromagnetic layers separated by a nonmagnetic gasket. [...] Read more.
This article performs computer simulations of the change in magnetization in the ferromagnetic film when polarized electric current passes through it. The model examines multilayer structures from ferromagnetic and nonmagnetic films. A sandwich system comprises two ferromagnetic layers separated by a nonmagnetic gasket. Ferromagnetic films have different magnetic susceptibility. The first ferromagnetic film is magnetically hard and acts as a fixed layer. The second ferromagnetic film is magnetically soft, with a switched direction of magnetization. The current direction is perpendicular to the film plane (CPP geometry). Spin transfer is carried out by electrons that polarize in the first ferromagnetic film and transmit spin to the second ferromagnetic film. We use the Ising model to describe the magnetic properties of the system and the Metropolis algorithm to form the thermodynamic states of the spin system. Simulations are performed at temperatures below the Curie points for both materials. The result of computer simulation is the dependence of magnetization in the magnetically soft film on the current strength in the system. Calculations show that there is a critical value of the current at which the magnetization sign of the controlled film changes. The magnetization versus current plot is stepwise. The change in the magnetization sign is due to an increase in the polarization of the electron gas. The plot of electron gas polarization versus current is also stepwise. Full article
(This article belongs to the Section Thin Films and Interfaces)
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<p>System geometry. <math display="inline"><semantics> <mrow> <mi>N</mi> <mi>M</mi> </mrow> </semantics></math> is a nonmagnetic material. <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>F</mi> <mi>M</mi> </mrow> <mrow> <mn>1</mn> </mrow> </msub> </mrow> </semantics></math> is a magnetically hard material. <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>F</mi> <mi>M</mi> </mrow> <mrow> <mn>2</mn> </mrow> </msub> </mrow> </semantics></math> is a magnetically soft material.</p>
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<p>Plot of magnetization in magnetically soft film <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>m</mi> </mrow> <mrow> <mn>2</mn> </mrow> </msub> </mrow> </semantics></math> versus electric field strength <math display="inline"><semantics> <mrow> <mi>E</mi> </mrow> </semantics></math>.</p>
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<p>Plot of electric current density <math display="inline"><semantics> <mrow> <mi>j</mi> </mrow> </semantics></math> versus electric field strength <math display="inline"><semantics> <mrow> <mi>E</mi> </mrow> </semantics></math>.</p>
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<p>Plot of the magnetization in the second film <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>m</mi> </mrow> <mrow> <mn>2</mn> </mrow> </msub> </mrow> </semantics></math> versus the current in the system <math display="inline"><semantics> <mrow> <mi>j</mi> </mrow> </semantics></math>.</p>
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<p>Plots of the polarization for the electron gas in the first film <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>P</mi> </mrow> <mrow> <mn>1</mn> </mrow> </msub> </mrow> </semantics></math> (red line) and in the second film <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>P</mi> </mrow> <mrow> <mn>2</mn> </mrow> </msub> </mrow> </semantics></math> (black line) against the current <math display="inline"><semantics> <mrow> <mi>j</mi> </mrow> </semantics></math>.</p>
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<p>Plot of the polarization of the electron gas <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>P</mi> </mrow> <mrow> <mn>01</mn> </mrow> </msub> </mrow> </semantics></math> in the film supplying the electric current versus the current <math display="inline"><semantics> <mrow> <mi>j</mi> </mrow> </semantics></math>.</p>
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29 pages, 22889 KiB  
Article
FEA Assessment of Contact Pressure and Von Mises Stress in Gasket Material Suitability for PEMFCs in Electric Vehicles
by Soo-Hyun Park, Akeem Bayo Kareem, Woo Jeong Joo and Jang-Wook Hur
Inventions 2023, 8(5), 116; https://doi.org/10.3390/inventions8050116 - 14 Sep 2023
Cited by 2 | Viewed by 4400
Abstract
Ensuring the safety of electric vehicles is paramount, and one critical concern is the potential for hazardous hydrogen fuel leaks caused by the degradation of Proton-Exchange Membrane Fuel Cell (PEMFC) gasket materials. This study employs advanced techniques to address this issue. We leverage [...] Read more.
Ensuring the safety of electric vehicles is paramount, and one critical concern is the potential for hazardous hydrogen fuel leaks caused by the degradation of Proton-Exchange Membrane Fuel Cell (PEMFC) gasket materials. This study employs advanced techniques to address this issue. We leverage Finite Element Analysis (FEA) to rigorously assess the suitability of gasket materials for PEMFC applications, focusing on two crucial conditions: ageing and tensile stress. To achieve this, we introduce a comprehensive “dual degradation framework” that considers the effects of contact pressure and von Mises stress. These factors are instrumental in evaluating the performance and durability of Liquid Silicon Rubber (LSR) and Ethylene Propylene Diene Monomer (EPDM) materials. Our findings reveal the Yeoh model as the most accurate and efficient choice for ageing simulations, boasting a minimal Mean Absolute Percentage Error (MAPE) and computational time of just 0.27 s. In contrast, the Ogden model, while accurate, requires more computational resources. In assessing overall model performance using MAE, Root Mean Square Error (RMSE), and R-squared metrics, both LSR and EPDM materials proved promising, with LSR exhibiting superior performance in most areas. Furthermore, our study incorporates uniaxial tensile testing, which yields RMSE and MAE values of 0.30% and 0.40%, respectively. These results provide valuable insights into material behaviour under tensile stress. Our research underscores the pivotal role of FEA in identifying optimal gasket materials for PEMFC applications. Notably, LSR is a superior choice, demonstrating enhanced FEA modelling performance under ageing and tensile conditions. These findings promise to significantly contribute to developing safer and more reliable electric vehicles by advancing gasket material design. Full article
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<p>A breakdown of the PEMFC compartment.</p>
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<p>PEMFC Gasket Material Framework.</p>
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<p>PEMFC Gasket Experiment (<b>a</b>) Tensile Testing (<b>b</b>) Ageing Testing.</p>
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<p>A cross-section/schematic of the experimental procedure under gasket tensile testing.</p>
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<p>(<b>a</b>) Stress-Strain curve under biaxial and uniaxial tensile testing at 40% displacement. (<b>b</b>) Stress-Strain curve under ageing technique.</p>
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<p>The FEA process description (<b>a</b>) by importing the CAD file in Hypermesh, and exporting the mesh after specifying the drag in Hypermesh, (<b>b</b>) importing the mesh files into MARC, and Setting Geometry &amp; Mesh Model-entity types for models, (<b>c</b>) specifying the boundary conditions, and selecting strain energy function, (<b>d</b>) The curve of the graph is fitted through experimental data, and Turning the interpretation around to check the interpretation results.</p>
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<p>The FEA process description (<b>a</b>) by importing the CAD file in Hypermesh, and exporting the mesh after specifying the drag in Hypermesh, (<b>b</b>) importing the mesh files into MARC, and Setting Geometry &amp; Mesh Model-entity types for models, (<b>c</b>) specifying the boundary conditions, and selecting strain energy function, (<b>d</b>) The curve of the graph is fitted through experimental data, and Turning the interpretation around to check the interpretation results.</p>
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<p>Contact Pressure and Von Mises Stress modelling visualization considering Mooney Rivlin and Yeoh Parameters under tensile conditions for PEMFC LSR gasket material.</p>
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<p>Contact Pressure and Von Mises Stress modelling visualization considering Ogden and Arruda Boyce Parameters under tensile conditions for PEMFC LSR gasket material.</p>
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<p>Contact Pressure and Von Mises Stress modelling visualization considering Gent and Neo Hookean Parameters under tensile conditions for PEMFC LSR gasket material.</p>
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<p>Contact Pressure and Von Mises Stress modelling visualization considering Mooney and Yeoh parameters under ageing conditions for PEMFC LSR gasket materials.</p>
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<p>Contact Pressure and Von Mises Stress modelling visualization considering for Ogden and Arruda Boyce Parameters under ageing conditions PEMFC LSR gasket materials.</p>
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<p>Contact Pressure and Von Mises Stress modelling visualization considering Gent and Neo Hookean Parameters under ageing conditions for PEMFC LSR gasket materials.</p>
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<p>Contact Pressure output data from FEA modelling considering the multi-hyperelastic models for EPDM and LSR gasket materials.</p>
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<p>Von Mises Stress output considering the multi-hyperelastic models at 40% displacement for EPDM and LSR PEMFC gasket material.</p>
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<p>Curve fitting assessment from multi-hyperelastic models under ageing conditions for PEMFC EPDM and LSR PEMFC gasket materials.</p>
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<p>Curve fitting assessment from multi-hyperelastic models under tensile conditions for PEMFC EPDM gasket material.</p>
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<p>Curve fitting assessment from multi-hyperelastic models under tensile conditions for PEMFC LSR gasket material.</p>
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<p>Regression metrics for EPDM and LSR PEMFC gasket materials considering ageing conditions.</p>
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<p>MAPE Metrics for EPDM and LSR PEMFC gasket materials considering tensile conditions.</p>
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<p>RMSE and MAE metrics for EPDM and LSR PEMFC gasket materials considering tensile conditions.</p>
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<p>Contact Pressure and Von Mises Stress modelling visualization considering Mooney Rivlin and Yeoh Parameters under tensile conditions for PEMFC EPDM gasket material.</p>
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<p>Contact Pressure and Von Mises Stress modelling visualization considering Ogden and Arruda Boyce Parameters under tensile conditions for PEMFC EPDM gasket material.</p>
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<p>Contact Pressure and Von Mises Stress modelling visualization considering Gent and Neo Hookean Parameters under tensile conditions for PEMFC EPDM gasket material.</p>
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<p>Contact Pressure and Von Mises Stress modelling visualization considering Mooney and Yeoh Parameters under ageing conditions for PEMFC EPDM material.</p>
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<p>Contact Pressure and Von Mises Stress modelling visualization considering Ogden and Arruda Boyce Parameters under ageing conditions for PEMFC EPDM materials.</p>
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<p>Contact Pressure and Von Mises Stress modelling visualization considering Gent and Neo Hookean Parameters under ageing conditions for PEMFC EPDM materials.</p>
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25 pages, 8256 KiB  
Article
Basic Design Parameters Influencing on Axial Stiffness of the Spiral Wound Gasket
by Przemysław Jaszak, Rafał Grzejda, Janusz Kluczyński and Paweł Zmarzły
Materials 2023, 16(18), 6209; https://doi.org/10.3390/ma16186209 - 14 Sep 2023
Cited by 2 | Viewed by 1440
Abstract
The article presents the influence of important design parameters of a spiral gasket on axial stiffness and leakage level. These parameters were the angle of inclination of the central part of the spiral section, the length of the vertical part of the spiral [...] Read more.
The article presents the influence of important design parameters of a spiral gasket on axial stiffness and leakage level. These parameters were the angle of inclination of the central part of the spiral section, the length of the vertical part of the spiral section, and the degree of densification of the material filling the metal coils. The scope of work was divided into two stages. In the first, experimental tests were conducted to determine the stiffness and tightness of a standard spiral gasket at two extreme levels of densification of the filler material, and the elastic–plastic properties of expanded graphite, which is the filler material of the metal spirals, were determined. In the second stage, multivariate numerical calculations were carried out to determine the axial stiffness of the gasket and to evaluate the distribution of contact pressure on the sealing surface. A novel aspect of the work is the proposal of a mathematical model to estimate the averaged value of the modulus of elasticity of the filler material as a function of the degree of densification and the execution of an experimental plan that significantly allowed the adoption of a limited number of analysed model variants used in the numerical calculations. Full article
(This article belongs to the Section Construction and Building Materials)
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<p>Samples used in the experimental studies: (<b>a</b>) first variant of the spiral gasket with graphite filler and a winding density of 0.9 turns/mm; (<b>b</b>) second variant of the gasket with a winding density of 1.4 turns/mm; (<b>c</b>) disc made of expanded graphite.</p>
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<p>Test stand for the determination of the elastic–plastic characteristics and tightness characteristics of the sealing materials.</p>
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<p>An example of an axisymmetric model of a gasket.</p>
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<p>Variables describing the cross-sectional shape of the spiral part of the gasket.</p>
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<p>Full geometric model prepared for the numerical calculations.</p>
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<p>Numbering of the individual variants of the cross-sections of the geometric models.</p>
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<p>Finite element mesh of the analysed computational model.</p>
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<p>Axisymmetric model of the gasket together with the lower and upper plates of the hydraulic press, which was used in the numerical calculations.</p>
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<p>Characteristics of the axial stiffness of the gasket with a low and high degree of winding density.</p>
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<p>Tightness characteristics of the gasket with regard to the winding density.</p>
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<p>Characteristics describing the contact pressure exerted on the surface of the sample with regard to its axial compression.</p>
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<p>Method of determining the local value of Young’s modulus based on the material compression curve.</p>
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<p>Effective width of the spiral part of the gasket.</p>
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<p>Graphical presentation of the surface area under the curve of the filler compression, which represents the local value of the modulus of elasticity.</p>
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<p>Maps of the reduced stress distribution for nine cases of the analysed gasket structures.</p>
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<p>Stiffness characteristics of the nine variants of the gasket construction.</p>
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<p>Distribution of the contact pressure for the nine variants of the gasket.</p>
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<p>Distribution of the axial stiffness in the gaskets in the case of variable parameters <span class="html-italic">x</span><sub>2</sub> and <span class="html-italic">x</span><sub>3</sub>, and the constant value of parameter <span class="html-italic">x</span><sub>1</sub> = −1.</p>
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<p>Two-dimensional (2D)—distribution of the axial stiffness in the gaskets in the case of variable parameters <span class="html-italic">x</span><sub>2</sub> and <span class="html-italic">x</span><sub>3</sub>, and the constant value of parameter <span class="html-italic">x</span><sub>1</sub> = −1.</p>
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<p>Distribution of the axial stiffness in the gaskets in the case of variable parameters <span class="html-italic">x</span><sub>2</sub> and <span class="html-italic">x</span><sub>3</sub>, and the constant value of parameter <span class="html-italic">x</span><sub>1</sub> = 0.</p>
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<p>Distribution of the axial stiffness in the gaskets in the case of variable parameters <span class="html-italic">x</span><sub>2</sub> and <span class="html-italic">x</span><sub>3</sub>, and the constant value of parameter <span class="html-italic">x</span><sub>1</sub> = 1.</p>
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18 pages, 5409 KiB  
Article
Research on Design and Optimization of Large Metal Bipolar Plate Sealing for Proton Exchange Membrane Fuel Cells
by Jinghui Zhao, Huijin Guo, Shaobo Ping, Zimeng Guo, Weikang Lin, Yanbo Yang, Wen Shi, Zixi Wang and Tiancai Ma
Sustainability 2023, 15(15), 12002; https://doi.org/10.3390/su151512002 - 4 Aug 2023
Cited by 4 | Viewed by 3200
Abstract
The sealing system, as the most important load-bearing component, is a critical part of the stack assembly in a proton exchange membrane fuel cell (PEMFC). Currently, flat or single-peak sealing gaskets are commonly used for large metal bipolar plate sealing, which can easily [...] Read more.
The sealing system, as the most important load-bearing component, is a critical part of the stack assembly in a proton exchange membrane fuel cell (PEMFC). Currently, flat or single-peak sealing gaskets are commonly used for large metal bipolar plate sealing, which can easily cause problems such as significant internal stress and distortion displacement. In order to solve this problem, an innovative double-peak sealing gasket structure is proposed. Based on the Mooney–Rivlin constitutive model, the impact of the sealing material hardness, friction coefficient, and compression ratio on the sealing performance are investigated. Meanwhile, the double-peak seal is fabricated and assembled into a single fuel cell for testing. The results show that the sealing performance of a double-peak sealing gasket with extended wings has been optimized, and the maximum contact pressure on the upper and lower contact surfaces is 1.2 MPa and 0.67 MPa, respectively, which is greater than the given air pressure of 0.1 MPa. And the sealing effect is optimal with a 45 Shore A hardness rubber, a friction coefficient of 0.05, and an initial compression ratio of 35%. The simulation and experimental sealing performance of the sealing gasket under different compression ratios remain similar. Full article
(This article belongs to the Special Issue Lithium Batteries and Fuel Cells for a Sustainable Future)
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<p>Geometric model of the metal bipolar plate. (<b>a</b>) Aligned sealing groove structure, (<b>b</b>) misaligned sealing groove structure.</p>
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<p>Schematic diagram of the seal structure design models. (<b>a</b>) Seal structure NO. 1, (<b>b</b>) seal structure NO. 2, (<b>c</b>) seal structure NO. 3, (<b>d</b>) the offset seal structure.</p>
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<p>Schematic diagram of sealing gasket under encapsulation force and air working pressure.</p>
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<p>Schematic diagram of the pressure-drop method’s leak detection principle.</p>
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<p>Installation effect of the gasket on the metal bipolar plate. (<b>a</b>) Gasket bonded to the bipolar plate. (<b>b</b>) Gasket bonded to the MEA.</p>
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<p>The path-flow procedures of the research on the double-peak sealing structure.</p>
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<p>Pressure distribution on the contact surface of the seal structure NO. 1 gasket. (<b>a</b>) Sealing structure, (<b>b</b>) upper contact surface, (<b>c</b>) lower contact surface.</p>
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<p>Pressure distribution on the contact surface of the seal structure NO. 1 gasket with the upper gasket was shifted 0.05 mm to the left. (<b>a</b>) Sealing structure, (<b>b</b>) upper contact surface, (<b>c</b>) lower contact surface.</p>
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<p>Pressure distribution on the contact surface of the seal structure NO. 2 gasket. (<b>a</b>) Sealing structure, (<b>b</b>) upper contact surface, (<b>c</b>) lower contact surface.</p>
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<p>Equivalent stress distribution of the double-peak sealing gasket with extended wings.</p>
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<p>Pressure distribution on the contact surface of the seal structure NO. 3 gasket. (<b>a</b>) Sealing structure, (<b>b</b>) upper contact surface, (<b>c</b>) lower contact surface.</p>
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<p>Pressure distribution on the contact surface of the offset sealing structure NO. 4 gasket. (<b>a</b>) Sealing structure, (<b>b</b>) upper contact surface, (<b>c</b>) lower contact surface.</p>
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<p>Relationship between the upper and lower contact surface pressure and hardness. (<b>a</b>) Pressure distribution diagram, (<b>b</b>) fitted curve.</p>
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<p>Relationship between the upper and lower contact surface pressure and friction coefficient. (<b>a</b>) Pressure distribution diagram. (<b>b</b>) Line chart.</p>
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<p>Relationship between the upper and lower contact surface pressure and compression ratio. (<b>a</b>) Pressure distribution diagram. (<b>b</b>) Fitted curve.</p>
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17 pages, 25985 KiB  
Article
High Temperature Friction and Wear Behavior of PTFE/MoS2 Composites
by Jinming Zhen, Yunxiang Han, Huabao Wang, Zhenguo Jiang, Li Wang, Yuqiang Huang, Zhengfeng Jia and Ran Zhang
Lubricants 2023, 11(8), 312; https://doi.org/10.3390/lubricants11080312 - 25 Jul 2023
Cited by 3 | Viewed by 2527
Abstract
High performance polymer matrix composites with low friction and wear rate are of urgent requirement in sliding bearings and gaskets. In this study, the PTFE/MoS2 composites were prepared and the effect of testing temperature on the tribological properties were investigated. Results show [...] Read more.
High performance polymer matrix composites with low friction and wear rate are of urgent requirement in sliding bearings and gaskets. In this study, the PTFE/MoS2 composites were prepared and the effect of testing temperature on the tribological properties were investigated. Results show that the friction coefficient and wear rate are approximately (0.14–0.19) and (4.18–13.38 × 10−4 mm3/Nm) at testing temperatures from 25 to 250 °C, respectively. At testing temperatures above 200 °C, the coefficient of friction of the composite with the addition of MoS2 is lower than that of pure PTFE, while the wear rate of the composite material with the addition of 2 wt.% and 5 wt.% MoS2 is lower than that of pure PTFE at temperatures above 150 °C. At low testing temperatures (25–100 °C), the main wear mechanism is that of slight abrasive wear, while from 150 °C to 250 °C, the main wear mechanism transformed to fatigue and severe abrasive wear. Full article
(This article belongs to the Special Issue Recent Advances in High Temperature Tribology)
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<p>Macro photograph of the (<b>a</b>) hot pressing sintering equipment (<b>b</b>) HT-1000 high temperature tribotester.</p>
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<p>Schematic diagram of contact form.</p>
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<p>Friction coefficients of four samples of PTFE composites as a function of testing temperatures.</p>
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<p>The typical friction curve of four composites at different testing temperatures: (<b>a</b>) 25 °C, (<b>b</b>) 50 °C, (<b>c</b>) 100 °C, (<b>d</b>) 150 °C, (<b>e</b>) 200 °C, (<b>f</b>) 250 °C.</p>
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<p>The typical friction curve of four composites at different testing temperatures: (<b>a</b>) 25 °C, (<b>b</b>) 50 °C, (<b>c</b>) 100 °C, (<b>d</b>) 150 °C, (<b>e</b>) 200 °C, (<b>f</b>) 250 °C.</p>
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<p>Wear rate of PTFE matrix composites as a function of testing temperatures.</p>
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<p>Cross-section profiles of the wear rate for four composites at different testing temperatures: (<b>a</b>) 25 °C, (<b>b</b>) 50 °C, (<b>c</b>) 200 °C, (<b>d</b>) 250 °C.</p>
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<p>SEM images of the worn surface for the P composite at different temperatures: (<b>a</b>) 25 °C, (<b>b</b>) 50 °C, (<b>c</b>) 200 °C, (<b>d</b>) 250 °C.</p>
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<p>SEM images of the worn surface for the PM1 composite at different temperatures: (<b>a</b>) 25 °C, (<b>b</b>) 50 °C, (<b>c</b>) 200 °C, (<b>d</b>) 250 °C.</p>
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<p>SEM images of the worn surface for the PM1 composite at different temperatures: (<b>a</b>) 25 °C, (<b>b</b>) 50 °C, (<b>c</b>) 200 °C, (<b>d</b>) 250 °C.</p>
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<p>SEM images of the worn surface for the PM2 composite at different temperatures: (<b>a</b>) 25 °C, (<b>b</b>) 50 °C, (<b>c</b>) 200 °C, (<b>d</b>) 250 °C.</p>
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<p>SEM images of the worn surface at 25 °C: (<b>a</b>) P, (<b>b</b>) PM1, (<b>c</b>) PM2, (<b>d</b>) PM5.</p>
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<p>SEM images of the worn surface at 25 °C: (<b>a</b>) P, (<b>b</b>) PM1, (<b>c</b>) PM2, (<b>d</b>) PM5.</p>
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<p>SEM images of the worn surface at 50 °C: (<b>a</b>) P, (<b>b</b>) PM1, (<b>c</b>) PM2, (<b>d</b>) PM5.</p>
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<p>SEM images of the worn surface at 100 °C: (<b>a</b>) P, (<b>b</b>) PM1, (<b>c</b>) PM2, (<b>d</b>) PM5.</p>
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<p>SEM images of the worn surface at 150 °C: (<b>a</b>) P, (<b>b</b>) PM1, (<b>c</b>) PM2, (<b>d</b>) PM5.</p>
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<p>SEM images of the worn surface at 150 °C: (<b>a</b>) P, (<b>b</b>) PM1, (<b>c</b>) PM2, (<b>d</b>) PM5.</p>
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<p>SEM images of the worn surface at 200 °C: (<b>a</b>) P, (<b>b</b>) PM1, (<b>c</b>) PM2, (<b>d</b>) PM5.</p>
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<p>SEM images of the worn surface at 250 °C: (<b>a</b>) P, (<b>b</b>) PM1, (<b>c</b>) PM2, (<b>d</b>) PM5.</p>
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<p>SEM images of the worn surface at 250 °C: (<b>a</b>) P, (<b>b</b>) PM1, (<b>c</b>) PM2, (<b>d</b>) PM5.</p>
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<p>Raman spectrum of the worn surfaces at 250 °C for the four composites.</p>
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<p>Raman spectrum of the worn surfaces at different testing temperatures for PM2.</p>
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12 pages, 3600 KiB  
Article
Antigorite Dehydration under Compression and Shear Loadings in a Rotational Diamond Anvil Cell
by Dayong Tan, Changguo Jiang, Weishan Chen, Yi Tan, Binbin Yue and Wansheng Xiao
Minerals 2023, 13(7), 871; https://doi.org/10.3390/min13070871 - 28 Jun 2023
Viewed by 1311
Abstract
Mineral dehydration in the subduction zone enormously affects Earth’s geodynamics and the global geochemical cycles of elements. This work uses Raman spectroscopy and X-ray diffraction to investigate the dehydration process of antigorite under compression and shear loading conditions in a rotational diamond anvil [...] Read more.
Mineral dehydration in the subduction zone enormously affects Earth’s geodynamics and the global geochemical cycles of elements. This work uses Raman spectroscopy and X-ray diffraction to investigate the dehydration process of antigorite under compression and shear loading conditions in a rotational diamond anvil cell (RDAC) at room temperature. In order to compare the shear effects, T301 stainless steel and Kapton plastic are applied as the gasket materials. In the experiment using a high-strength T301 stainless steel gasket, two new broad OH-stretching peaks of H2O and H3O2 appear at 3303 and 3558 cm−1, respectively, at 1.7 GPa. The original sharp OH-stretching peaks of antigorite at 3668 and 3699 cm−1 remain, while the central pressure is increased to 8.0 GPa, and the largest pressure gradient is about 2.5 GPa in the sample chamber. In another experiment with a low-strength gasket of Kapton plastic, two new OH-stretching broad peaks of H2O and H3O2 also start to appear at 3303 and 3558 cm−1, respectively, at a lower pressure of 0.3 GPa, but the original sharp OH-stretching peaks of antigorite at 3668 and 3699 cm−1 almost completely vanish as the central pressure reaches 3.0 GPa, with the largest pressure gradient at around 4.8 GPa. The comparison between the two experiments shows that antigorite is easier to dehydrate in the chamber of a Kapton plastic gasket with a larger gradient of shear stress. However, its axial compression stress is lower. The high-pressure Raman spectra of MgO2(OH)4 octahedron and SiO4 tetrahedron in the low wavenumber zones (100–1200 cm−1) combined with the micro-beam X-ray diffraction spectrum of the recovered product strongly support the structural breakdown of antigorite. This investigation reveals that the water-bearing silicate minerals have strong shear dehydration in the cold subduction zone of the plate, which has important applications in predicting the physical and chemical properties of subduction zones and deducing the rate of plate subduction. Full article
(This article belongs to the Special Issue Water in Mantle Minerals)
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<p>Rotational diamond anvil cell and the compression and shear loadings.</p>
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<p>Representative Raman spectra of antigorite with T301 gasket in the range of 100–1200 cm<sup>−1</sup> under compression and shear loading.</p>
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<p>Representative Raman spectra of antigorite with T301 gasket in the range of 2750–5000 cm<sup>−1</sup> under compression and shear loading.</p>
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<p>Dependence of shear stress on the rotation angle in the chamber at the central pressure of 5.0 (<b>a</b>) and 8.0 GPa (<b>b</b>). The insert is the distribution of the measurement points.</p>
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<p>Representative Raman spectra of antigorite with Kapton plastic gasket in the range of 100–1200 cm<sup>−1</sup> under compression and shear loading.</p>
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<p>Representative Raman spectra of antigorite with Kapton plastic gasket in the range of 2750–5000 cm<sup>−1</sup> under compression and shear loading.</p>
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<p>Dependence of shear stress on the rotation angle in the chamber at the central pressures of 1.3 (<b>a</b>) and 3.0 GPa (<b>b</b>). The inset is the distribution of the measurement points.</p>
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<p>X-ray diffraction spectra of the starting material and recovered product and the structure index.</p>
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15 pages, 5534 KiB  
Article
Mechanical Aging Test and Sealing Performance of Thermoplastic Vulcanizate as Sealing Gasket in Automotive Fuel Cell Applications
by Hyungu Im and Sunkyoung Jeoung
Polymers 2023, 15(8), 1872; https://doi.org/10.3390/polym15081872 - 13 Apr 2023
Cited by 10 | Viewed by 2741
Abstract
Ethylene–propylene–diene monomer (EPDM) rubber is one of the rapidly developing synthetic rubbers for use as a gasket material in proton exchange membrane (PEM) fuel cell applications. Despite its excellent elastic and sealing properties, EPDM faces challenges such as molding processability and recycling ability. [...] Read more.
Ethylene–propylene–diene monomer (EPDM) rubber is one of the rapidly developing synthetic rubbers for use as a gasket material in proton exchange membrane (PEM) fuel cell applications. Despite its excellent elastic and sealing properties, EPDM faces challenges such as molding processability and recycling ability. To overcome these challenges, thermoplastic vulcanizate (TPV), which comprises vulcanized EPDM in polypropylene matrix, was investigated as a gasket material for PEM fuel cell applications. TPV showed better long-term stability in terms of tension and compression set behaviors under accelerated aging conditions than EPDM. Additionally, TPV exhibited significantly higher crosslinking density and surface hardness than EPDM, regardless of the test temperature and aging time. TPV and EPDM showed similar leakage rates for the entire range of test inlet pressure values, regardless of the applied temperature. Therefore, we can conclude that TPV exhibits a similar sealing capability with more stable mechanical properties compared with commercialized EPDM gaskets in terms of He leakage performance. Full article
(This article belongs to the Special Issue Polymer Materials for Energy Storage and Fuel Cells Applications)
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<p>Comparison of tensile thermal oxidation aging results: (<b>a</b>) tensile strength changes of EPDM; (<b>b</b>) tensile strength changes of TPV.</p>
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<p>Comparison of CS thermal oxidation aging results: (<b>a</b>) CS changes of EPDM; (<b>b</b>) CS changes of TPV.</p>
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<p>The crosslinking properties of EPDM and TPV: (<b>a</b>) swelling ratio changes of EPDM and TPV in cyclohexane; (<b>b</b>) calculated crosslinking density values of EPDM and TPV.</p>
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<p>Comparison of FTIR spectra of pristine and thermal oxidized EPDM: (<b>a</b>) full-range scan results; (<b>b</b>,<b>c</b>) peaks assigned to CH<sub>2</sub> stretching and vibration; (<b>d</b>,<b>e</b>) peaks assigned to carbonyl stretching and vibration.</p>
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<p>Comparison of FTIR spectra of pristine and thermal oxidized EPDM: (<b>a</b>) full-range scan results; (<b>b</b>,<b>c</b>) peaks assigned to CH<sub>2</sub> stretching and vibration; (<b>d</b>,<b>e</b>) peaks assigned to carbonyl stretching and vibration.</p>
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<p>Mechanical property changes under acid conditions: (<b>a</b>) surface hardness changes; (<b>b</b>) CS changes.</p>
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<p>Surface photomicrographs of pristine and aged materials under 90 °C acidic condition; (<b>a</b>) pristine EPDM, (<b>b</b>) aged EPDM, (<b>c</b>) pristine TPV, and (<b>d</b>) aged TPV.</p>
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<p>Experimental fixture for evaluation of leakage performance in gasket stack: (<b>a</b>) schematic diagram of overall fixture; (<b>b</b>) cross-section schematic diagram of fixture; (<b>c</b>) image of gasket and sealing plate; (<b>d</b>) image of assembled test fixture.</p>
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<p>Comparison of leakage rates of gasket materials prepared in this study with results from the literature.</p>
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13 pages, 4802 KiB  
Article
Numerical Simulation of Assembly Process and Sealing Reliability of T-Rubber Gasket Pipe Joints
by Yang Han, Guoqi Han, Dongqiao Li, Junfeng Duan and Yewen Yan
Sustainability 2023, 15(6), 5160; https://doi.org/10.3390/su15065160 - 14 Mar 2023
Cited by 2 | Viewed by 1799
Abstract
Underground pipelines are vital parts to urban water supply, gas supply, and other lifeline systems, affecting the sustainable development of cities to a great extent. The pipeline joint, which is a weak link, may be seriously damaged during natural disasters such as earthquakes. [...] Read more.
Underground pipelines are vital parts to urban water supply, gas supply, and other lifeline systems, affecting the sustainable development of cities to a great extent. The pipeline joint, which is a weak link, may be seriously damaged during natural disasters such as earthquakes. The failure of pipe joints can cause leakage accidents, resulting in system failure and interruption, and even some secondary disasters. Herein, based on uniaxial and plane tensile test results of a T-rubber gasket material, the assembly process and sealing performance of a T-rubber gasket joint of a ductile iron pipe are numerically simulated using the Ogden third-order strain energy density function to fit the material constant. The simulation accounts for severe nonlinearities, including large deformations, hyperelasticity, and complex contacts. The effects of the assembly friction coefficient, assembly depth, and radial clearance deviation of the socket and spigot on the seal contact pressure are analyzed. The results suggest that the entire history of the deformation and stress variations during assembly can be clearly visualized and accurately calculated. For the different friction coefficients, the assembly depth corresponding to the sliding friction condition of the spigot pipe was 74 mm, while the minimum pushing force required to assemble the T-rubber gasket joint of a DN300 ductile iron pipe was 6.8 kN at the ideal situation with a friction coefficient of 0. The effective contact pressure of the rubber gasket seepage surface under various operating conditions is much higher than the normal pressure of municipal pipelines, thus indicating that the rubber gasket joint exhibits the ideal sealing performance. Furthermore, a certain deviation, which is about 20 mm, is allowed for the assembly depth of the rubber gasket joint such that the axial displacement of the pipe joint can be adapted under an earthquake or ground displacement. Full article
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<p>Calculated dimensions of pipe joint and T-rubber gasket: (<b>a</b>) T-rubber gasket joint; (<b>b</b>) T- rubber gasket.</p>
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<p>FEM model.</p>
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<p>Tests for determining basic mechanical properties of T-rubber gasket materials: (<b>a</b>) Uniaxial tensile test (UT); (<b>b</b>) Plane tensile test (PT).</p>
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<p>Test results of two types of rubber: (<b>a</b>) Shore hardness of 50; (<b>b</b>) Shore hardness of 88.</p>
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<p>Comparison between test and fitting results: (<b>a</b>) Shore hardness of 50; (<b>b</b>) Shore hardness of 88.</p>
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<p>Installation process of T-shaped rubber gasket (units: MPa).</p>
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<p>Assembly process of pipe interface (units: MPa).</p>
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<p>Relationship between propulsion force and assembly depth during intubation installation.</p>
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<p>Contact pressure of seepage surface of T-shaped rubber gasket: (<b>a</b>) Contact surface of the spigot; (<b>b</b>) Contact surface of the socket.</p>
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<p>Relationship between propulsion force and assembly depth under different friction coefficients.</p>
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<p>Contact pressure distributions of T-shaped rubber gasket under different friction coefficients: (<b>a</b>) Contact surface of the spigot; (<b>b</b>) Contact surface of the socket.</p>
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<p>Contact pressure distribution of T-shaped rubber ring under different assembly depths: (<b>a</b>) Contact surface of the spigot; (<b>b</b>) Contact surface of the socket.</p>
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<p>Contact pressure distribution of T-shaped rubber ring under different values of radial clearance: (<b>a</b>) Contact surface of the spigot; (<b>b</b>) Contact surface of the socket.</p>
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20 pages, 7387 KiB  
Article
Investigation of Warning Thresholds for the Deformation of GINA Gasket of Immersed Tunnel Based on a Material-to-Mechanical Analysis
by Hao Ding, Jingsong Huang, Xinghong Jiang, Yu Yan, Shouji Du, Juntao Chen and Qing Ai
Mathematics 2023, 11(4), 1010; https://doi.org/10.3390/math11041010 - 16 Feb 2023
Cited by 1 | Viewed by 2182
Abstract
As the first waterproof component of the immersed tunnel, it is very important to ensure the remaining compression of the GINA gasket to resist external water intrusion. This paper proposed a method for determining warning thresholds for the remaining compression of the GINA [...] Read more.
As the first waterproof component of the immersed tunnel, it is very important to ensure the remaining compression of the GINA gasket to resist external water intrusion. This paper proposed a method for determining warning thresholds for the remaining compression of the GINA gasket based on a material-to-mechanical analysis. In terms of material analysis, two factors that affect the GINA gasket are investigated: rubber hardness and cross-sectional shape, and they are adopted as the basis for subsequent mechanical analysis. In terms of mechanical analysis, uneven settlement during the operation period is considered to be the major cause of joint deformation, which is further divided into four modes: bending, shear, expansion, and torsion, with the computation model of the GINA gasket established to obtain the warning threshold. After that, a graded early warning method is adopted, and corresponding thresholds are given after an investigation of previous studies, which are validated by a three-dimensional finite element analysis. The deformation monitoring data between the E28 and E29 elements of the Hong Kong–Zhuhai–Macao Bridge Immersed Tunnel are used to verify the proposed method. The results show that the GINA gasket of the Hong Kong–Zhuhai–Macao Bridge Immersed Tunnel is currently in a safe state, and its deformation is much lower than the minimum warning level. Full article
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Figure 1
<p>The different types of immersed tunnel joints (redrawn according to Wei and Lu [<a href="#B17-mathematics-11-01010" class="html-bibr">17</a>] and Xue [<a href="#B18-mathematics-11-01010" class="html-bibr">18</a>]). (<b>a</b>) Semi-flexible to semi-rigid joint. (<b>b</b>) Semi-rigid joint. (<b>c</b>) Flexible joint.</p>
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<p>Stiffness–deformation curve of the GINA gasket (redrawn according to the results of Peng et al. [<a href="#B19-mathematics-11-01010" class="html-bibr">19</a>]).</p>
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<p>The traditional GINA gasket (redrawn according to Xiao et al. [<a href="#B10-mathematics-11-01010" class="html-bibr">10</a>]).</p>
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<p>The different cross-sectional shapes of GINA gaskets (redrawn according to Hu et al. [<a href="#B23-mathematics-11-01010" class="html-bibr">23</a>]).</p>
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<p>The four typical types of GINA gaskets (redrawn according to Hu et al. [<a href="#B23-mathematics-11-01010" class="html-bibr">23</a>]).</p>
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<p>The relationship curve between the minimum compression and water pressure (redrawn according to the results of Tang, Guan and Wan [<a href="#B24-mathematics-11-01010" class="html-bibr">24</a>]).</p>
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<p>The relationship of compression characteristics of GINA gasket (redrawn according to Liu et al. [<a href="#B25-mathematics-11-01010" class="html-bibr">25</a>]).</p>
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<p>The four deformation modes of immersed tunnel joint (redrawn according to Xie et al. [<a href="#B26-mathematics-11-01010" class="html-bibr">26</a>]): (<b>a</b>) bending; (<b>b</b>) shear; (<b>c</b>) expansion; (<b>d</b>) torsion.</p>
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<p>The four deformation modes of immersed tunnel joint (redrawn according to Xie et al. [<a href="#B26-mathematics-11-01010" class="html-bibr">26</a>]): (<b>a</b>) bending; (<b>b</b>) shear; (<b>c</b>) expansion; (<b>d</b>) torsion.</p>
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<p>Geometric diagram of bending deformation.</p>
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<p>Geometric diagram of shear deformation.</p>
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<p>Geometric diagram of expansion deformation.</p>
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<p>Longitudinal layout of the HZMB immersed tunnel (redrawn according to Lin et al. [<a href="#B41-mathematics-11-01010" class="html-bibr">41</a>]).</p>
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<p>Cross-sectional geometry of the HZMB immersed tunnel (unit: cm).</p>
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<p>The compressive stress–deformation curve of the GINA gasket (redrawn according to Lin and Liu [<a href="#B42-mathematics-11-01010" class="html-bibr">42</a>]).</p>
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<p>Mechanical decomposition of the deformation modes of immersed tunnel joint between E28 and E29 elements.</p>
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<p>Total change of the compression of GINA gasket between E28 and E29 elements varying with time.</p>
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<p>Geometry and finite element mesh of GINA gasket.</p>
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<p>Stresses of GINA gasket under design compression (MPa).</p>
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<p>Bottom pressure of GINA gasket under different remaining compressions: (<b>a</b>) range of bottom pressure; (<b>b</b>) remaining compression = 108 mm; (<b>c</b>) remaining compression = 97.2 mm; (<b>d</b>) remaining compression = 86.4 mm.</p>
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14 pages, 5697 KiB  
Article
Glass–Zirconia Composites as Seals for Solid Oxide Cells: Preparation, Properties, and Stability over Repeated Thermal Cycles
by Magdalena Kosiorek, Agnieszka Żurawska, Leszek Ajdys, Anna Kolasa, Yevgeniy Naumovich, Paulina Wiecińska, Aleksey Yaremchenko and Jakub Kupecki
Materials 2023, 16(4), 1634; https://doi.org/10.3390/ma16041634 - 15 Feb 2023
Cited by 2 | Viewed by 2443
Abstract
This study focuses on the preparation and characterization of composite gaskets designed for the sealing of the solid oxide cell stacks operating below 700 °C. The seals were fabricated with the addition of various amounts (10–90 wt.%) of 3 mol.% yttria partially stabilized [...] Read more.
This study focuses on the preparation and characterization of composite gaskets designed for the sealing of the solid oxide cell stacks operating below 700 °C. The seals were fabricated with the addition of various amounts (10–90 wt.%) of 3 mol.% yttria partially stabilized zirconia to a BaO-Al2O3-CaO-SiO2 glass matrix. The sample gaskets in the form of thin frames were shaped by tape casting. The quality of the junctions between the composites and Crofer 22APU steel commonly used as an SOC interconnect was evaluated after thermal treatment of heating to 710 °C, then cooling to the working temperature of around 620 °C and then leaving them for 10h in an air atmosphere, before cooling to room temperature. The samples were also studied after 3, 5, and 10 thermal cycles to determine the changes in microstructure and to evaluate the porosity and possible crystallization of the glass phase. The compression of the seals was calculated on the basis of differences in thickness before and after thermal treatment. The influence of zirconia additions on the mechanical properties of the seals was studied. The experimental results confirmed that glass–ceramic composites are promising materials for gaskets in SOC stacks. The most beneficial properties were obtained for a composite containing 40 wt.% of YSZ. Full article
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<p>Diagram of a sample in the form of a composite frame sandwiched between Crofer 22APU steel.</p>
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<p>Microstructure and histogram of the grain size distribution of glass powder Schott GM31107 (<b>a</b>–<b>c</b>) and YSZ powder (<b>d</b>–<b>f</b>).</p>
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<p>XRD pattern of Schott glass GM31107 powder.</p>
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<p>Cross-sections of the obtained samples consisting of 0–70 wt.% YSZ: (<b>a</b>) reference glass sample, (<b>b</b>) composite with 10 wt.% YSZ, (<b>c</b>) composite with 20 wt.% YSZ, (<b>d</b>) composite with 30 wt.% YSZ, (<b>e</b>) composite with 40 wt.% YSZ, (<b>f</b>) composite with 50 wt.% YSZ, (<b>g</b>) composite with 60 wt.% YSZ, and (<b>h</b>) composite with 70 wt.% YSZ.</p>
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<p>Porosity of the glass and composite layers after the sealing procedure vs. YSZ content.</p>
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<p>Compression rate and initial thickness of the sample seals after the heating procedure vs. YSZ content.</p>
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<p>XRD patterns of the glass and composite samples containing 10–50 wt.% YSZ after the thermal treatment cycle.</p>
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<p>Results of SEM observations of the pure glass and 40 wt.% YSZ composite samples that underwent repeated thermal cycles: (<b>a</b>) glass after 3 cycles, (<b>b</b>) glass after 5 cycles, (<b>c</b>) glass after 10 cycles, (<b>d</b>) composite after 3 cycles, (<b>e</b>) composite after 5 cycles, (<b>f</b>) and composite after 10 cycles.</p>
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15 pages, 2412 KiB  
Article
Packaging Materials Based on Styrene-Isoprene-Styrene Triblock Copolymer Modified with Graphene
by Traian Zaharescu and Cristina Banciu
Polymers 2023, 15(2), 353; https://doi.org/10.3390/polym15020353 - 9 Jan 2023
Cited by 2 | Viewed by 1981
Abstract
This study presents the improved stabilization effects of graphene on a polymer substrate, namely a styrene-isoprene-styrene triblock copolymer (SIS) which creates opportunities for long-term applications and radiation processing. The added graphene has a remarkable activity on the protection of polymer against their oxidation [...] Read more.
This study presents the improved stabilization effects of graphene on a polymer substrate, namely a styrene-isoprene-styrene triblock copolymer (SIS) which creates opportunities for long-term applications and radiation processing. The added graphene has a remarkable activity on the protection of polymer against their oxidation due to the penetration of free macroradical fragments into the free interlayer space. The chemiluminescence procedure used for the evaluation of the progress of oxidation reveals the delaying effect of oxidative degradation by the doubling extension of oxidation induction time, when the material formulation containing graphene is oxidized at 130 °C. The pristine polymer that is thermally aged requires an activation energy of 142 kJ mol−1, while the modified material needs 148, 158 and 169 kJ mol−1, for the oxidative degradation in the presence of 1, 2 and, respectively, 3 wt% of graphene. The contribution of graphene content (1 wt%) on the stability improvement of SIS is demonstrated by the increase of onset oxidation temperature from 190 °C for neat polymer to 196 °C in the presence of graphene and to 205 °C for the polymer stabilized with graphene and rosemary extract. The addition of graphene into the polymer formulations is a successful method for enlarging durability instead of the modification of receipt with synthesis antioxidants. The presumable applications of these studied materials cover the areas of medical wear, food packaging, commodities, sealing gaskets and others that may also be included through the products for nuclear power plants. Full article
(This article belongs to the Collection Assessment of the Ageing and Durability of Polymers)
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<p>FTIR spectrum of prepared reduced graphene oxide.</p>
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<p>(<b>a</b>) Nonisothermal CL spectra recorded on pristine SIS samples subjected to a thermal ageing treatment at 80 °C at various heating times. (1) 0 h; (2) 5 h; (3) 10 h; (4) 15 h; (5) 20 h. Measurement heating rate: 10 °C·min<sup>−1</sup>; (<b>b</b>) histogram of CL intensity determined at two main temperatures (the color code is identical for the both figures).</p>
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<p>(<b>a</b>) Nonisothermal CL spectra recorded on SIS/graphene (1 wt%) samples after their thermal ageing treatment at 80 °C at various heating times. (1) 0 h; (2) 5 h; (3) 10 h; (4) 15 h; (5) 20 h; (<b>b</b>) nonisothermal CL spectra recorded on SIS (6) and SIS/graphene (1 wt%)/rosemary (0.5 wt%) (7) samples without pre-ageing. The heating rate of all measurement: 10 °C min<sup>−1</sup>.</p>
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<p>The nonisothermal CL curves recorded on the SIS samples improved by graphene (1 wt%)/rosemary (0.5 wt%) couple after their thermal ageing at 80 °C at various heating times. Heating rate: 10 °C min<sup>−1</sup>.</p>
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<p>Isothermal CL spectra for neat SIS samples after their thermal treatment at 80 °C for various heating times. Heating temperature: 80 °C. Testing temperature: 130 °C. The mentioned figures denote the time of thermal treatment.</p>
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<p>Isothermal CL spectra recorded on the samples of SIS containing different graphene loadings; measurement temperature: 130 °C.</p>
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<p>The isothermal CL spectra recorded on SIS samples modified by various graphene loadings. (<b>a</b>) free of additive; (<b>b</b>) graphene 1 wt%; (<b>c</b>) graphene 2 wt%; (<b>d</b>) graphene 3 wt%; Testing temperatures: (1) 130 °C; (2) 140 °C; (3) 150 °C.</p>
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