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Search Results (203)

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Keywords = cryogenic treatment

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16 pages, 4812 KiB  
Article
Electrical and Dielectrical Properties of Composites Based on Alumina and Cyclic Olefin Copolymers
by Eusebiu Ilarian Ionete, Artur Visse, Radu Dorin Andrei, Mirela Irina Petreanu, Stefan Ionut Spiridon and Roxana Elena Ionete
Materials 2024, 17(21), 5349; https://doi.org/10.3390/ma17215349 - 31 Oct 2024
Viewed by 412
Abstract
Understanding the performance of polymer dielectrics at different temperatures is becoming increasingly important due to the rapid development of electric cars, electromagnetic devices, and new energy production solutions. Cyclic olefin copolymers (COCs) are an attractive material due to their low water absorption, good [...] Read more.
Understanding the performance of polymer dielectrics at different temperatures is becoming increasingly important due to the rapid development of electric cars, electromagnetic devices, and new energy production solutions. Cyclic olefin copolymers (COCs) are an attractive material due to their low water absorption, good electrical insulation, long-term stability of surface treatments, and resistance to a wide range of acids and solvents. This work focused on the dielectric and electrical properties of cyclic olefin copolymer (COC)/Al2O3 composites over a wide range of temperature and frequency domains, from room temperature to cryogenic temperatures (around 125 K). Permittivity, electrical conductivity, and electrical modulus are given consideration. A composite of up to 50% Al2O3 mixed with COC was prepared via a conventional melt-blending method. The final samples were formed in sheets and processed using injection and extrusion moldings. It was found that formulations with Al2O3 concentrations ranging from 10 to 50% resulted in higher electrical conductivity while maintaining the viscosity of the composite at a level acceptable for polymer-processing machinery. Our data show that COC/alumina composites present substantial potential as materials for high-frequency applications, even at the regime of cryogenic temperatures. Full article
(This article belongs to the Section Polymeric Materials)
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<p>Image of the capacitor cell within the spectrometer.</p>
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<p>Dielectric constant against frequency for the base COC6 and the most modified variant (COC6-50) across temperatures (353 K, 303 K, 173 K, and 123 K).</p>
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<p>Dielectric loss for COC6 and COC6-50 at the lowest and highest investigation temperatures.</p>
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<p>Modulus <span class="html-italic">M′</span>: comparison between COC6 and COC6-50 at different temperatures.</p>
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<p>Modulus <span class="html-italic">M”</span>: comparison between COC6 and COC6-50 at the lowest and highest testing temperatures (123 K and 353 K, respectively).</p>
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<p>Overlapped thermal gravimetric curves for polymer sample (COC 100%) and composite (COC + x% Al<sub>2</sub>O<sub>3</sub>) samples.</p>
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<p>Heat flux variation curves for cyclic olefin copolymer (COC) samples with varying proportions of alumina (0%, 10%, 20%, 30%, 40%, and 50% Al<sub>2</sub>O<sub>3</sub>).</p>
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<p>The glass transition point (T<sub>g</sub>), determined from the heat flow variation curve.</p>
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<p>Comparative XRD spectra for all COC6 (cyclic olefin copolymer) composites with added alumina particles vs. pristine COC6. Miller indices for major peaks correspond to the prevailing alumina phase as identified during analysis (Al<sub>2</sub>O<sub>3</sub> vs. Al<sub>2.4</sub>O<sub>3.6</sub>). The initial broad peak around 16° corresponds to the amorphous COC6 phase.</p>
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18 pages, 6821 KiB  
Article
Effect of Cryogenic Treatment on Residual Stress and Microstructure of 6061 Aluminum Alloy and Optimization of Parameters
by Xuemei Niu, Zhi Chen, Linwang Jing, Yao Huang and Yuhang Liu
Materials 2024, 17(19), 4873; https://doi.org/10.3390/ma17194873 - 4 Oct 2024
Viewed by 728
Abstract
Residual stress induced by solution treatment in 6061 aluminum alloy can lead to workpiece deformation, or even premature failure. The efficiency of traditional heat treatment for relieving residual stress is relatively low. Therefore, this study introduces a novel cryogenic treatment technique to reduce [...] Read more.
Residual stress induced by solution treatment in 6061 aluminum alloy can lead to workpiece deformation, or even premature failure. The efficiency of traditional heat treatment for relieving residual stress is relatively low. Therefore, this study introduces a novel cryogenic treatment technique to reduce residual stress. The optimal cryogenic process parameters were achieved by orthogonal experiments: cryogenic temperature of 113 K, holding time of 24 h, 1 cryogenic cycle, and a cooling rate of 3 K·min−1, and the residual stress of aluminum alloy was measured by the blind hole method. The microstructural evolutions in 6061 aluminum alloy were tested by OM, SEM, and TEM. The results show that the introduction of cryogenic treatment can reduce residual stress in 6061 aluminum alloy by 64%, mainly due to the reduction of dislocations and the uniform distribution of β’’ phase. Full article
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<p>Heat treatment flowchart.</p>
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<p>The schematic diagram shows the dimension of the sample and the test location of residual stress.</p>
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<p>Diagram showing the dimension of tensile specimens.</p>
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<p>(<b>a</b>) Residual stress values of samples treated by different processes, and (<b>b</b>) residual stress elimination rates of samples treated by different processes.</p>
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<p>The OM images of samples treated by different processes: (<b>a</b>) sample 0; (<b>b</b>) sample 2; (<b>c</b>) sample 5; and (<b>d</b>) sample 7.</p>
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<p>The SEM and EDS images of samples treated by different processes: (<b>a</b>,<b>b</b>) sample 0; (<b>c</b>,<b>d</b>) sample 2; (<b>e</b>,<b>f</b>) sample 5; and (<b>g</b>,<b>h</b>) sample 7.</p>
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<p>TEM images of specimens treated with different processes: (<b>a</b>) sample 0; and (<b>b</b>) sample 5.</p>
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<p>TEM images of specimens treated with different processes: (<b>a</b>,<b>b</b>) sample 0; and (<b>c</b>,<b>d</b>) sample 5.</p>
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<p>Grain refinement, dislocation movement and second phase precipitation mechanism.</p>
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<p>The results of samples with different treatments: (<b>a</b>) hardness; and (<b>b</b>) mechanical properties.</p>
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<p>The fracture morphology of samples treated by different processes: (<b>a</b>) sample 0; (<b>b</b>) sample 2; (<b>c</b>) sample 5; and (<b>d</b>) sample 7.</p>
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20 pages, 11340 KiB  
Article
Synergistic Effects of Surface Texture and Cryogenic Treatment on the Tribological Performance of Aluminum Alloy Surfaces
by Rui Liu, Xiwen Deng, Xuejian Sun, Jilin Lei, Dewen Jia, Wengang Chen and Qiang Ji
Lubricants 2024, 12(10), 336; https://doi.org/10.3390/lubricants12100336 - 30 Sep 2024
Viewed by 651
Abstract
In order to improve the tribological properties of the 7075-T6 aluminum alloy used on the rotor surface, a combined method of cryogenic treatment and laser surface texture treatment was applied. Various tests, including metallographic microscopy, scanning electron microscopy, elemental analysis, microhardness measurements, were [...] Read more.
In order to improve the tribological properties of the 7075-T6 aluminum alloy used on the rotor surface, a combined method of cryogenic treatment and laser surface texture treatment was applied. Various tests, including metallographic microscopy, scanning electron microscopy, elemental analysis, microhardness measurements, were conducted to examine the wear morphology and modification mechanism of the treated 7075-T6 aluminum alloy surface. A numerical simulation model of surface texture was established using computational fluid dynamics to analyze the lubrication characteristics of V-shaped texture. The research finding that the 7075-T6 aluminum alloy experienced grain refinement during the cryogenic treatment process, enhancing the wear resistance of the V-shaped textures. This improvement delayed the progression of fatigue wear, abrasive wear, and oxidative wear, thereby reducing friction losses. The designed V-shaped texture contributes to reducing contact area, facilitating the capture and retention of abrasives, and enhancing oil film load-bearing capacity, thereby improving tribological performance. The synergistic effect of cryogenic treatment reduced the friction coefficient by 24.8% and the wear loss by 66.4%. Thus, the combination of surface texture and cryogenic treatment significantly improved the tribological properties of the 7075-T6 aluminum alloy. Full article
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<p>Rotor-seal wear.</p>
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<p>Texture preparation of specimen surfaces.</p>
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<p>Friction and wear experimental testing.</p>
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<p>Texture simulation model.</p>
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<p>Grid model diagram of texture: (<b>a</b>) The relationship between the average pressure on the internal surface of the texture and the number of grids; (<b>b</b>) Grid model of texture.</p>
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<p>Microhardness of specimens with different heat treatment processes (The error line represents the standard error).</p>
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<p>Microstructure of different process treatments: (<b>a</b>,<b>b</b>) under OM; (<b>c</b>–<b>f</b>) under SEM.</p>
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<p>Energy dispersive spectroscopy (EDS) results for coarse two-phase particles.</p>
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<p>Texture topography.</p>
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<p>Pressure distribution and velocity vector distribution in the fluid domain.</p>
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<p>Friction coefficient versus time.</p>
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<p>Average friction coefficients of different samples (Corresponding to the average friction coefficient in <a href="#lubricants-12-00336-f011" class="html-fig">Figure 11</a>).</p>
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<p>Metallurgical microscope wear marks: (<b>a</b>) ST; (<b>b</b>) SCT; (<b>c</b>) SAT; (<b>d</b>) SCAT; (<b>e</b>) STT; (<b>f</b>) SCTT; (<b>g</b>) SATT; (<b>h</b>) SCATT.</p>
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<p>Amount of wear and tear on the sample (The error line represents the standard error).</p>
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<p>3D images of wear mark (<b>a</b>) SAT; (<b>b</b>) SCAT; (<b>c</b>) SATT; (<b>d</b>) SCATT.</p>
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<p>Wear patterns of fabrics (<b>a</b>) STT; (<b>b</b>) SCTT; (<b>c</b>) SATT; (<b>d</b>) SCATT.</p>
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<p>Schematic diagram of friction mechanism: (<b>a</b>) Schematic representation illustrating the improvement of friction mechanism through cryogenic treatment; (<b>b</b>) Schematic representation of the friction mechanism with surface texture, b-I is a schematic diagram of abrasive particle generation, b-II is the mechanism diagram of texture wear reduction.</p>
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11 pages, 2477 KiB  
Article
Cyclic Loading of Metallic Glasses Prepared Using Cryogenic Treatments
by Nicolás Amigo
Corros. Mater. Degrad. 2024, 5(4), 439-449; https://doi.org/10.3390/cmd5040020 - 26 Sep 2024
Viewed by 669
Abstract
This study investigates the degradation of mechanical properties in CuZr metallic glasses (MGs) under cyclic loading using molecular dynamics simulations. Both as-cast (AC) and cryogenically thermal-cycled (TC) samples with Cu36Zr64 and Cu64Zr36 compositions were analyzed. Results show [...] Read more.
This study investigates the degradation of mechanical properties in CuZr metallic glasses (MGs) under cyclic loading using molecular dynamics simulations. Both as-cast (AC) and cryogenically thermal-cycled (TC) samples with Cu36Zr64 and Cu64Zr36 compositions were analyzed. Results show that cyclic loading significantly degrades Young’s modulus, ultimate tensile stress, and toughness, with most pronounced reductions occurring in the initial cycles. TC samples exhibit improved ductility and stability compared to AC samples. In contrast, AC samples demonstrate greater initial strength but faster degradation. Cu-rich samples maintain higher strength but degrade similarly to Cu-poor samples. The AC Cu-rich sample experiences more localized deformation and delayed degradation, while TC and AC Cu-poor samples quickly reach a steady state. These findings highlight the influence of atomic composition and thermal treatments on the mechanical performance and degradation behavior of MGs. Full article
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<p>The ten largest populations of voronoi polyhedra for the AC and TC samples.</p>
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<p>Stress–strain curves for the cyclic loading. AC and TC correspond to as-cast and thermal-cycling samples, respectively.</p>
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<p>(<b>a</b>) Young’s modulus, (<b>b</b>) ultimate tensile stress, (<b>c</b>) and toughness calculated in each cycle for each sample.</p>
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<p>Percentage difference of each mechanical property between the first and last cycle.</p>
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<p>Atomic shear strain fields for the samples at the end of the 1st, 3rd, and 5th cycle.</p>
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<p>(<b>a</b>) Degree of strain localization and (<b>b</b>) participation ratio for each sample.</p>
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<p>Variation of (<b>a</b>) solid-like polyhedra, (<b>b</b>) liquid-like polyhedra, and (<b>c</b>) average fivefold local symmetry during cyclic loading.</p>
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<p>Variation of per-atom potential energy during cyclic loading.</p>
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14 pages, 10797 KiB  
Article
The Influence of Deep Cryogenic Treatment (DCT) on the Microstructure Evolution and Mechanical Properties of TC4 Titanium Alloy
by Xuzhi Lan, Yulang Xu, Jingyong Li, Yifeng Gong and Mingxiao Shi
Materials 2024, 17(18), 4603; https://doi.org/10.3390/ma17184603 - 19 Sep 2024
Viewed by 600
Abstract
Deep cryogenic treatment (−196 °C, DCT) is an emerging application that can make significant changes to many materials. In this study, DCT was applied to Ti6Al4V (TC4) titanium alloy, and we delved into an examination of the impact on its microstructural morphologies and [...] Read more.
Deep cryogenic treatment (−196 °C, DCT) is an emerging application that can make significant changes to many materials. In this study, DCT was applied to Ti6Al4V (TC4) titanium alloy, and we delved into an examination of the impact on its microstructural morphologies and mechanical properties. It was observed that DCT has a significant effect on the grain refinement of the TC4 titanium alloy base material. Obvious grain refinement behavior can be observed with 6 h of DCT, and the phenomenon of grain refinement becomes more pronounced with extension of the DCT time. In addition, DCT promotes the transformation of the β phase into the α′ phase in the TC4 titanium alloy base material. XRD analysis further confirmed that DCT leads to the transformation of the β phase into the α′ phase. The element vanadium was detected by scanning electron microscopy, and it was found that the β phase inside the base material had transformed into the α′ phase. It was observed that DCT has a positive influence on the hardness of the TC4 titanium alloy base material. The hardness of the sample treated with 18 h of DCT increased from 331.2 HV0.5 to 362.5 HV0.5, presenting a 9.5% increase compared to the sample without DCT. Furthermore, it was proven that DCT had little effect on the tensile strength but a significant impact on the plasticity and toughness of the base material. In particular, the elongation and impact toughness of the sample subject to 18 h of DCT represented enhancements of 27.33% and 8.09%, respectively, compared to the raw material without DCT. Full article
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<p>Metallographic structure of the base material treated with different DCT times: (<b>a</b>) 0 h, (<b>b</b>) 6 h, (<b>c</b>) 12 h, (<b>d</b>) 18 h, and (<b>e</b>) 24 h. (<b>f</b>) Percentage content of β.</p>
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<p>XRD diffraction patterns. (<b>a</b>) XRD diffraction patterns of the base material treated with different DCT times, (<b>b</b>) Patitial XRD patterns of (<b>a</b>).</p>
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<p>SEM morphologies of the base material treated with different DCT times: (<b>a</b>) 0 h, (<b>b</b>) 6 h, (<b>c</b>) 12 h, (<b>d</b>) 18 h, and (<b>e</b>) 24 h.</p>
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<p>EDS results in the raw material without DCT. (<b>a</b>) Scanning electron microscopy morphology, (<b>b</b>) Element content of point 1, (<b>c</b>) Element content of point 2.</p>
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<p>EDS results in the base material treated with 18 h of DCT. (<b>a</b>) Scanning electron microscopy morphology, (<b>b</b>) Element content of point1, (<b>c</b>) Element content of point.</p>
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<p>EBSD orientation maps of base material with and without DCT. (<b>a</b>) IPF—0 h, (<b>b</b>) Grain boundary diagram—0 h, (<b>c</b>) IPF—18 h, (<b>d</b>) Grain boundary diagram—18 h.</p>
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<p>Phase characteristics of base material with and without DCT: (<b>a</b>) 0 h and (<b>b</b>) 18 h.</p>
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<p>KAM maps of base material with and without DCT: (<b>a</b>) 0 h and (<b>b</b>) 18 h.</p>
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<p>Transmission electron microscopy morphology of base material with and without DCT. (<b>a</b>,<b>c</b>): 0 h; (<b>b</b>,<b>d</b>): 18 h.</p>
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<p>Microhardness of the base metal treated with different DCT times.</p>
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<p>Tensile properties of the base metal with different DCT times.</p>
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<p>The tensile fracture morphologies of the base metal with different DCT times: (<b>a</b>) 0 h, (<b>b</b>) 6 h, (<b>c</b>) 12 h, (<b>d</b>) 18 h, and (<b>e</b>) 24 h.</p>
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<p>Impact properties of the base metal with different DCT times.</p>
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<p>The impact fracture morphologies of the base metal treated with different DCT times: (<b>a</b>) 0 h, (<b>b</b>) 6 h, (<b>c</b>) 12 h, (<b>d</b>) 18 h, and (<b>e</b>) 24 h.</p>
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12 pages, 7771 KiB  
Article
A Study on the Liquid Helium Temperature Tensile Property of Fe-21Cr-15Ni-5Mn-2Mo Austenitic Stainless Steel after Solution Treatment
by Mengxing Zhang, Changjun Wang, Dangshen Ma, Yu Liu, Weijun Wang, Jianxiong Liang, Chao Fang, Weihan Chu and Chuanjun Huang
Materials 2024, 17(18), 4597; https://doi.org/10.3390/ma17184597 - 19 Sep 2024
Viewed by 550
Abstract
A novel non-magnetic Fe-21Cr-15Ni-5Mn-2Mo austenitic stainless steel with high strength and plasticity has been developed. The microstructure and liquid helium temperature (4.2 K) tensile properties of the top and bottom samples of large-size forged flat steel after solution treatment at 1090 °C were [...] Read more.
A novel non-magnetic Fe-21Cr-15Ni-5Mn-2Mo austenitic stainless steel with high strength and plasticity has been developed. The microstructure and liquid helium temperature (4.2 K) tensile properties of the top and bottom samples of large-size forged flat steel after solution treatment at 1090 °C were investigated. The results showed that the average grain size of the bottom sample (48.0 ± 6.7 μm) was smaller than that of the top sample (58.8 ± 15.3 μm), and the MX precipitates and Z phases were distributed in the matrix of the samples. The 4.2 K strengths of the samples at the top and bottom were high, and large amounts of annealing twin boundaries played a certain role in strengthening. After cryogenic tensile testing, large amounts of deformation twins, stacking faults, and dislocations were generated inside the austenite grains of both samples, which helped the material to obtain higher plasticity and strength. The top and bottom samples possessed excellent synergies of strength and plasticity at 4.2 K, and the 4.2 K tensile properties of the top sample were as follows: ultimate tensile strength (UTS) of 1850 MPa, yield strength (YS) of 1363 MPa, and elongation (EL) of 26%. The tested steel is thus believed to meet the requirements of combined excellent strength and plasticity within a deep cryogenic environment, and it would be a promising material candidate for manufacturing superconducting coil cases to serve in new generation fusion engineering. Full article
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<p>Schematic illustration of test specimens taken from prototype steel forging.</p>
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<p>The equilibrium phase diagram.</p>
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<p>(<b>a</b>,<b>b</b>) Microstructures; (<b>c</b>,<b>d</b>) austenite grains of bottom sample (<b>a</b>,<b>c</b>) and top sample (<b>b</b>,<b>d</b>).</p>
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<p>Precipitated phases observed using SEM. (<b>a</b>,<b>b</b>) Z phase and MX phase; (<b>c</b>–<b>e</b>) corresponding EDS of bottom sample (<b>a</b>,<b>c</b>) and top sample (<b>b</b>,<b>d</b>,<b>e</b>).</p>
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<p>Extracted powder XRD results of bottom sample and top sample.</p>
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<p>TEM observation. (<b>a</b>) Z phase and MX phase in bottom sample; (<b>b</b>) Z phase and MX phase in top sample; (<b>c</b>–<b>f</b>) SAED and EDS of Z phase and MX phase; (<b>c</b>,<b>e</b>) Z phase and (<b>d</b>,<b>f</b>) MX (NbN).</p>
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<p>(<b>a</b>) Tensile properties at 4.2 K of experimental steel; (<b>b</b>) stress–strain curves.</p>
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<p>Microhardness of top and bottom samples.</p>
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<p>EBSD analyses of samples before (<b>a</b>,<b>b</b>,<b>e</b>) and after (<b>c</b>,<b>d</b>,<b>f</b>) tensile fracture of top (<b>a</b>,<b>c</b>) and bottom (<b>b</b>,<b>d</b>) samples and misorientation distributions (<b>e</b>,<b>f</b>). Low angle grain boundaries, high angle grain boundaries and twinning grain boundaries are respectively shown in red, black and green lines in (<b>a</b>–<b>d</b>).</p>
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<p>Deformed microstructures after tensile test using SEM (<b>a</b>,<b>b</b>) and TEM (<b>c</b>,<b>d</b>) of top samples (<b>a</b>,<b>c</b>) and bottom samples (<b>b</b>,<b>d</b>).</p>
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18 pages, 5957 KiB  
Article
Temperature Effect on Deformation Mechanisms and Mechanical Properties of Welded High-Mn Steels for Cryogenic Applications
by Minha Park, Gang Ho Lee, Geon-Woo Park, Gwangjoo Jang, Hyoung-Chan Kim, Sanghoon Noh, Jong Bae Jeon, Byoungkoo Kim and Byung Jun Kim
Materials 2024, 17(16), 4159; https://doi.org/10.3390/ma17164159 - 22 Aug 2024
Viewed by 661
Abstract
High-manganese steel (high-Mn) is valuable for its excellent mechanical properties in cryogenic environments, making it essential to understand its deformation behavior at extremely low temperatures. The deformation behavior of high-Mn steels at extremely low temperatures depends on the stacking fault energy (SFE) that [...] Read more.
High-manganese steel (high-Mn) is valuable for its excellent mechanical properties in cryogenic environments, making it essential to understand its deformation behavior at extremely low temperatures. The deformation behavior of high-Mn steels at extremely low temperatures depends on the stacking fault energy (SFE) that can lead to the formation of deformation twins or transform to ε-martensite or α′-martensite as the temperature decreases. In this study, submerged arc welding (SAW) was applied to fabricate thick pipes for cryogenic industry applications, but it may cause problems such as an uneven distribution of manganese (Mn) and a large weldment. To address these issues, post-weld heat treatment (PWHT) is performed to achieve a homogeneous microstructure, enhance mechanical properties, and reduce residual stress. It was found that the difference in Mn content between the dendrite and interdendritic regions was reduced after PWHT, and the SFE was calculated. At cryogenic temperatures, the SFE decreased below 20 mJ/m2, indicating the martensitic transformation region. Furthermore, an examination of the deformation behavior of welded high-Mn steels was conducted. This study revealed that the tensile deformed, as-welded specimens exhibited ε and α′-martensite transformations at cryogenic temperatures. However, the heat-treated specimens did not undergo α′-martensite transformations. Moreover, regardless of whether the specimens were subjected to Charpy impact deformation before or after heat treatment, ε and α′-martensite transformations did not occur. Full article
(This article belongs to the Special Issue Advances in Solid-State Welding Processes)
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<p>(<b>a</b>) A schematic diagram of the PWHT process and (<b>b</b>) location of Charpy impact test specimen and tensile test specimen in welded high-Mn steel.</p>
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<p>The microstructure of welded high-Mn steel before and after heat treatment: (<b>a</b>) before heat treatment (as-welded) and (<b>b</b>) heat-treated at 1000 °C (W1000); Red box indicates the enlarged area of the weldment. Yellow arrows indicate dendrite growth direction.</p>
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<p>(<b>a</b>) EDS results for Mn content of welded high-Mn steel in dendrite and interdendritic areas before and after heat-treatment at 1000 °C. Each red arrow represents the difference in Mn content in the dendrite and interdendrite regions before and after heat treatment. (<b>b</b>) SFE of welded high-Mn steel in dendrite and interdendritic regions as function of temperature. The SFE was calculated by Curtze’s model.</p>
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<p>(<b>a</b>) Engineering stress–strain curves and (<b>b</b>) strain hardening rate of as-welded and W1000 specimens at room temperature and cryogenic temperature.</p>
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<p>X-ray diffraction (XRD) patterns for the as-welded and W1000 specimens before and after tensile deformation at the different temperatures: (<b>a</b>) Before deformation; (<b>b</b>) Tensile specimen fractured at room temperature (RT); and (<b>c</b>) Tensile specimen fractured at cryogenic temperature.</p>
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<p>EBSD inverse pole figure (IPF) map, phase map, and grain boundary (GB) map of the tensile fractured specimens at cryogenic temperature for the as-welded and W1000 specimens: (<b>a</b>) IPF map of as-welded, (<b>b</b>) phase map of as-welded, (<b>c</b>) GB map of as-welded, (<b>d</b>) IPF map of W1000, (<b>e</b>) phase map of W1000, and (<b>f</b>) GB map of W1000.</p>
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<p>Transmission electron micrograph of the welded high-Mn steel deformed at cryogenic temperature (−160 °C): (<b>a</b>) bright field image of as-welded specimen; (<b>b</b>) diffraction patterns of austenite (magenta line), twin (green line), ε and α′-martensite (yellow line and red line, respectively); (<b>c</b>) BF image of heat-treated specimen (W1000); and (<b>d</b>) diffraction patterns of austenite and twin.</p>
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<p>SEM fractography of as-welded specimen and W1000 specimen tensile tested at cryogenic temperature: (<b>a</b>) As-welded specimen and (<b>b</b>) W1000.</p>
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<p>Charpy impact absorbed energy and the load–displacement curves for as-welded and W1000 specimens acquired through instrumented Charpy impact test at room temperature (20 °C) and at cryogenic temperature (−160 °C): (<b>a</b>) Charpy impact absorbed energy, load–displacement curves (<b>b</b>) at room temperature (RT), and (<b>c</b>) at cryogenic temperature (CT).</p>
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<p>X-ray diffraction (XRD) patterns for the as-welded and W1000 specimens before and after impact deformation at the different temperatures: (<b>a</b>) Charpy impact specimen fractured at room temperature (RT) and (<b>b</b>) Charpy impact specimen fractured at cryogenic temperature (CT).</p>
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<p>EBSD inverse pole figure (IPF) map, phase map, and grain boundary (GB) map of welded high-Mn after Charpy impact fractured at room temperature (20 °C) and cryogenic temperature (−160 °C): (<b>a</b>) As-welded_RT, (<b>b</b>) W1000_RT, (<b>c</b>) As-welded_CT, and (<b>d</b>) W1000_CT.</p>
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10 pages, 6424 KiB  
Communication
Synergistic Strength–Ductility Improvement in an Additively Manufactured Body-Centered Cubic HfNbTaTiZr High-Entropy Alloy via Deep Cryogenic Treatment
by Zhuoheng Liang, Zhanggen Ye, Chunfeng Liu, Liangbo Sun and Yongzhong Zhang
Micromachines 2024, 15(8), 937; https://doi.org/10.3390/mi15080937 - 23 Jul 2024
Viewed by 613
Abstract
HfNbTaTiZr high-entropy alloy has wide application prospects as a biomedical material, and the use of laser additive manufacturing can solve the forming problems faced by the alloy. In view of the characteristics of the one-time forming of additive manufacturing methods, it is necessary [...] Read more.
HfNbTaTiZr high-entropy alloy has wide application prospects as a biomedical material, and the use of laser additive manufacturing can solve the forming problems faced by the alloy. In view of the characteristics of the one-time forming of additive manufacturing methods, it is necessary to develop non-mechanical processing modification methods. In this paper, deep cryogenic treatment (DCT) is first applied to the modification of a HEA with BCC structure, then the post-processing method of DCT is combined with laser melting deposition (LMD) technology to successfully realize the coordinated improvement of forming and strength–ductility synergistic improvement in lightweight Hf0.25NbTa0.25TiZr alloy. The final tensile strength of the alloy after DCT treatment is 25% higher than that of the as-cast alloy and 11% higher than that of the as-deposited alloy, and the elongation is increased by 48% and 10%, respectively. In addition, DCT also achieves induced phase transition without additional deformation. Full article
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<p>Raw materials, sample preparation methods, and DCT process schematics: (<b>a</b>) morphology and particle size of powder, (<b>b</b>) diagram of LMD system, (<b>c</b>) diagram of LMD forming and sampling, (<b>d</b>) cryogenic treatment temperature curve.</p>
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<p>XRD test results and residual stress calculation results: (<b>a</b>) XRD diffraction patterns of samples with different soaking times, (<b>b</b>) main diffraction peak amplification diagram, (<b>c</b>) calculated value of residual stress.</p>
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<p>Mechanical properties and microstructure of samples at different soaking times at room temperature: (<b>a</b>,<b>b</b>) tensile mechanical properties, (<b>c</b>–<b>g</b>) the microstructure of alloys with different DCT durations, (<b>h</b>) the phase precipitation of DCT120 sample, (<b>i</b>) amplification diagram and diffraction spots of precipitated phase, (<b>j</b>) element composition of precipitated phase.</p>
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<p>Schematic diagram of defect and residual stress formation during the DCT process: (<b>A</b>) Before DCT, (<b>B</b>) The beginning of DCT process, (<b>C</b>) The DCT process continues, (<b>D</b>) DCT process ends back to room temperature.</p>
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<p>(<b>a</b>) The model and (<b>b</b>) simulation results used in the numerical ABAQUS simulation of residual stress in DCT process.</p>
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13 pages, 4243 KiB  
Article
An Insight into the Varying Effects of Different Cryogenic Temperatures on the Microstructure and the Thermal and Compressive Response of a Mg/SiO2 Nanocomposite
by Michael Johanes, Sarah Mehtabuddin, Vishal Venkatarangan and Manoj Gupta
Metals 2024, 14(7), 808; https://doi.org/10.3390/met14070808 - 11 Jul 2024
Viewed by 667
Abstract
This study for the first time reports that insights into microstructure and thermal and compressive responses can be best achieved following exposure to different cryogenic temperatures and that the lowest cryogenic temperature may not always produce the best results. In the present study, [...] Read more.
This study for the first time reports that insights into microstructure and thermal and compressive responses can be best achieved following exposure to different cryogenic temperatures and that the lowest cryogenic temperature may not always produce the best results. In the present study, a Mg-SiO2 biocompatible and environment-friendly nanocomposite was synthesized by using the Disintegrated Melt Deposition method followed by hot extrusion. Subsequently, it was subjected to four different sub-zero temperatures (−20 °C, −50 °C, −80 °C, and −196 °C). The results reveal the best densification at −80 °C, marginally improved ignition resistance at 50 °C, the best damping response at −80 °C, the best microhardness at −50 °C, and the best compressive response at −20 °C. The results clearly indicate that the cryogenic temperature should be carefully chosen depending on the property that needs to be particularly enhanced governed by the principal requirement of the end application. Full article
(This article belongs to the Special Issue Design and Development of Metal Matrix Composites)
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<p>Scanning electron micrographs of Mg-2SiO<sub>2</sub> materials in this work, with selected regions used for the EDS studies.</p>
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<p>EDS results/chart of Mg-2SiO<sub>2</sub> AE: matrix region.</p>
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<p>X-ray diffractograms of Mg-2SiO<sub>2</sub> materials in this work.</p>
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<p>The ignition responses of Mg-2SiO<sub>2</sub> materials in this work, showing the locations where ignition temperatures were evaluated.</p>
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<p>Thermal response of Mg-2SiO<sub>2</sub> materials in this work.</p>
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<p>Macro-scale photographs of compressed Mg-2SiO<sub>2</sub> materials in this work.</p>
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<p>Fractographs of Mg-2SiO<sub>2</sub> materials in this work.</p>
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12 pages, 3752 KiB  
Article
Effect of Deep Cryogenic Treatment on the Artificial Aging Behavior of 6082 Aluminum Alloy
by Sawei Qiu, Jian Tang, Yiran Tian, Changping Wu, Tuo Ye, Erli Xia and Yuanzhi Wu
Coatings 2024, 14(6), 755; https://doi.org/10.3390/coatings14060755 - 14 Jun 2024
Viewed by 856
Abstract
This study investigates the impact of cryogenic treatment duration on the mechanical properties and microstructural evolution of 6082 aluminum alloy subjected to subsequent artificial aging. Tensile tests were conducted using an electronic universal testing machine, and the microstructure was characterized by employing optical [...] Read more.
This study investigates the impact of cryogenic treatment duration on the mechanical properties and microstructural evolution of 6082 aluminum alloy subjected to subsequent artificial aging. Tensile tests were conducted using an electronic universal testing machine, and the microstructure was characterized by employing optical microscopy (OM), scanning electron microscopy (SEM), and transmission electron microscopy (TEM). The results indicate that both the tensile strength and elongation of the alloy first increase and then decrease with the extension of cryogenic treatment duration. The alloy treated with 12 h of cryogenic treatment followed by artificial aging at 180 °C for 8 h achieved a peak strength of 390 MPa. Meanwhile, the alloy treated with 8 h of cryogenic treatment and the same artificial aging process reached a maximum elongation of 13%. All specimens of 6082 aluminum alloy subjected to cryogenic and aging treatments exhibited ductile fracture under room temperature tensile conditions. The size of dimples at the fracture surface first increased and then decreased with increasing cryogenic treatment duration, indicating a transition from deeper to shallower dimples. The cryogenic treatment did not significantly affect the grain size of the alloy, which remained approximately 230 µm on average. Cryogenic treatment facilitated the precipitation of fine, densely distributed precipitates, enhancing the pinning effect of dislocations and thus improving the tensile strength. Additionally, cryogenic treatment increased the dislocation density and promoted the formation of subgrains, while the grain boundary precipitates transitioned from a continuous to a discontinuous distribution, all of which contribute to the enhancement of the plasticity. Full article
(This article belongs to the Special Issue Microstructure, Mechanical and Tribological Properties of Alloys)
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<p>The size of tensile specimen (mm).</p>
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<p>Cryogenic treatment processes of the sample.</p>
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<p>Characterization region of the sample.</p>
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<p>True stress–strain curve of 6082 aluminum alloy under different cryogenic treatment.</p>
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<p>Variations of tensile strength as a function of orientation under different heat treatment conditions.</p>
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<p>Macro morphology of tensile fracture surface of alloy after different heat treatments: (<b>a</b>) DC 4 h + AA; (<b>b</b>) DC 12 h + AA; (<b>c</b>) DC 24 h + AA.</p>
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<p>Fracture morphology of tensile surface of 6082 alloy after different heat treatments: (<b>a</b>) DC 4 h + AA; (<b>b</b>) DC 12 h + AA; (<b>c</b>) DC 24 h + AA.</p>
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<p>OM of 6082 alloy after different heat treatments: (<b>a</b>) DC 4 h + AA undeformed; (<b>b</b>) DC 12 h + AA undeformed; (<b>c</b>) DC 24 h + AA undeformed; (<b>d</b>) DC 4 h + AA deformed; (<b>e</b>) DC 12 h + AA deformed; and (<b>f</b>) DC 24 h + AA deformed.</p>
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<p>TEM of 6082 alloy after different heat treatments: (<b>a</b>) DC 4 h + AA; (<b>b</b>) DC 12 h + AA; (<b>c</b>) DC 24 h + AA.</p>
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<p>TEM pictures of 6082 alloy after tension under different heat treatments: (<b>a</b>) DC 4 h + AA; (<b>b</b>) DC 12 h + AA; (<b>c</b>) DC 24 h + AA.</p>
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14 pages, 5078 KiB  
Article
Mechanical Properties and Microstructural Evolution of 6082 Aluminum Alloy with Different Heat Treatment Methods
by Erli Xia, Tuo Ye, Sawei Qiu, Jie Liu, Jiahao Luo, Longtao Sun and Yuanzhi Wu
Coatings 2024, 14(5), 602; https://doi.org/10.3390/coatings14050602 - 10 May 2024
Cited by 2 | Viewed by 1182
Abstract
The influence of solid solution treatment (SST), artificial aging treatment (AAT), and deep cryogenic-aging treatment (DCAT) on the mechanical properties and microstructure evolution of 6082 aluminum alloy was investigated. The tensile test was performed to obtain the true stress–strain curves through an electronic [...] Read more.
The influence of solid solution treatment (SST), artificial aging treatment (AAT), and deep cryogenic-aging treatment (DCAT) on the mechanical properties and microstructure evolution of 6082 aluminum alloy was investigated. The tensile test was performed to obtain the true stress–strain curves through an electronic universal testing machine. The results show that the yield strengths of the SST specimens in all three directions are the lowest, of less than 200 MPa. In addition, the maximum elongation of the SST specimen is over 16% and the value of in-plane anisotropy (IPA) is 5.40%. For the AAT specimen, the yield strengths of the AAT alloy in three directions have distinct improvements, which are beyond 340 MPa. However, the maximum elongation and the IPA were evidently reduced. The yield strength and elongation of the DCAT alloy exhibit a slight enhancement compared with those in the AAT condition, and the corresponding IPA is 0.61%. The studied alloy specimens in all conditions exhibit ductile fracture. The DCAT alloy has the highest density of precipitates with the smallest size. Therefore, the dislocation pinning effect of the DCAT specimens are the strongest, which exhibit the highest yield strength accordingly. In addition, the uniformly distributed precipitates in the matrix with a large ratio of long and short axes can suppress the anisotropy caused by elongated grains. Full article
(This article belongs to the Special Issue Microstructure, Mechanical and Tribological Properties of Alloys)
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<p>Schematic diagrams of specimen size (<b>a</b>) and specimen orientation (<b>b</b>).</p>
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<p>The illustration of the heat treatment process.</p>
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<p>Diagram of the specimen microstructural observation zone.</p>
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<p>The true stress–strain curves under different heat treatment processes: (<b>a</b>) as-received; (<b>b</b>) SST; (<b>c</b>) AAT; and (<b>d</b>) DCAT.</p>
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<p>The relationship between yield strength and specimen orientation.</p>
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<p>The fracture morphology of 6082 aluminum alloy with different heat treatment conditions: (<b>a</b>) SST 0°; (<b>b</b>) SST 45°; (<b>c</b>) SST 90°; (<b>d</b>) AAT 0°; (<b>e</b>) AAT 45°; (<b>f</b>) AAT 90°; (<b>g</b>) DCAT 0°; (<b>h</b>) DCAT 45°; and (<b>i</b>) DCAT 90°.</p>
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<p>The microstructure of the 6082 aluminum alloy with different heat treatment conditions before the tensile test: (<b>a</b>) as-received; (<b>b</b>) SST; (<b>c</b>) AAT; and (<b>d</b>) DCAT.</p>
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<p>The microstructure near fracture of the 6082 aluminum alloy with different heat treatment conditions after the tensile experiment (<b>a</b>) SST 0°; (<b>b</b>) SST 45°; (<b>c</b>) SST 90°; (<b>d</b>) as-received 0°; (<b>e</b>) AAT 0°; and (<b>f</b>) DCAT 0°.</p>
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<p>The microstructure near fracture of the 6082 aluminum alloy with different heat treatment conditions after the tensile experiment (<b>a</b>) SST 0°; (<b>b</b>) SST 45°; (<b>c</b>) SST 90°; (<b>d</b>) as-received 0°; (<b>e</b>) AAT 0°; and (<b>f</b>) DCAT 0°.</p>
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<p>TEM images of 6082 aluminum alloy with different heat treatment conditions before the tensile test: (<b>a</b>) as-received; (<b>b</b>) SST; (<b>c</b>) AAT; and (<b>d</b>) DCAT.</p>
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<p>TEM images of the 6082 aluminum alloy with different heat treatment conditions after the tensile test: (<b>a</b>) as-received; (<b>b</b>) SST; (<b>c</b>) AAT; and (<b>d</b>) DCAT.</p>
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<p>TEM images of the 6082 aluminum alloy with different heat treatment conditions after the tensile test: (<b>a</b>) as-received; (<b>b</b>) SST; (<b>c</b>) AAT; and (<b>d</b>) DCAT.</p>
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21 pages, 4602 KiB  
Review
Effects of Cryogenic- and Cool-Assisted Burnishing on the Surface Integrity and Operating Behavior of Metal Components: A Review and Perspectives
by Jordan Maximov and Galya Duncheva
Machines 2024, 12(5), 312; https://doi.org/10.3390/machines12050312 - 2 May 2024
Cited by 2 | Viewed by 1545
Abstract
When placed under cryogenic temperatures (below −180 °C), metallic materials undergo structural changes that can improve their service life. This process, known as cryogenic treatment (CrT), has received extensive research attention over the past five decades. CrT can be applied as either an [...] Read more.
When placed under cryogenic temperatures (below −180 °C), metallic materials undergo structural changes that can improve their service life. This process, known as cryogenic treatment (CrT), has received extensive research attention over the past five decades. CrT can be applied as either an autonomous process (for steels and non-ferrous alloys, tool materials, and finished products) or as an assisting process for conventional metalworking. Cryogenic impacts and conventional machining or static surface cold working (SCW) can also be performed simultaneously in hybrid processes. The static SCW, known as burnishing, is a widely used environmentally friendly finishing process that achieves high-quality surfaces of metal components. The present review is dedicated to the portion of the hybrid processes in which burnishing under cryogenic conditions is carried out from the viewpoint of surface engineering, namely, finishing–surface integrity (SI)–operational behavior. Analyzes and summaries of the effects of cryogenic-assisted (CrA) burnishing on SI and the operational behavior of the investigated materials are made, and perspectives for future research are proposed. Full article
(This article belongs to the Topic Advanced Manufacturing and Surface Technology)
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<p>Fields of application of cryogenic treatment.</p>
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<p>Types of cryogenic processes.</p>
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<p>Schemes of cryogenic-assisted burnishing methods: 1—multiple ball burnishing; 2—roller burnishing with cylindrical roller; 3—roller burnishing with toroidal roller; 4—ball burnishing with hydrostatic sphere; 5—slide burnishing with spherical-ended insert; 6—slide burnishing with cylindrical-ended insert; 7—slide-roller burnishing; 8—ball burnishing with undefined ball motion.</p>
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<p>Percentage share of the studied materials: 1—magnesium alloys; 2—titanium alloys; 3—aluminum alloys; 4—steels; 5—additively manufactured materials; 6—biomaterials; 7—thermal spray coatings.</p>
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<p>Percentage share of the used burnishing methods: SB—slide burnishing; DB—diamond burnishing; BBHS—ball burnishing with hydrostatic sphere; BB—ball burnishing; RB—roller burnishing.</p>
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<p>Percentage share of SI characteristics (<b>a</b>) and operating behavior (<b>b</b>): R—roughness; MH—microhardness; RS—residual stresses; M—microstructure; F—fatigue; WR—wear resistance; CR—corrosion resistance.</p>
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<p>Comparison of the effects of DR on the roughness and microhardness of Ti-6Al-4V under different cooling conditions.</p>
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<p>Influence of the burnishing force and the burnishing conditions on the obtained surface microhardness of Inconel 718.</p>
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<p>Influence of DB conditions on the surface axial residual stress and the surface microhardness of 17-4 PH martensitic stainless steel.</p>
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<p>Influence of the temperature during the DR process on the surface axial residual stresses and the corresponding number of cycles to failure of 304 austenitic stainless steel.</p>
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<p>S-N curves of 304 austenitic stainless steel [<a href="#B41-machines-12-00312" class="html-bibr">41</a>].</p>
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16 pages, 15580 KiB  
Article
Improving the Tribological Properties of WE43 and WE54 Magnesium Alloys by Deep Cryogenic Treatment with Precipitation Hardening in Linear Reciprocating Motion
by Adrian Barylski, Krzysztof Aniołek, Grzegorz Dercz, Izabela Matuła, Sławomir Kaptacz, Jan Rak and Robert Paszkowski
Materials 2024, 17(9), 2011; https://doi.org/10.3390/ma17092011 - 25 Apr 2024
Cited by 1 | Viewed by 1093
Abstract
This paper presents the results of tribological tests on WE43 and WE54 magnesium alloys with rare earth metals performed in linear reciprocating motion for four different material couples (AISI 316-L steel, silicon nitride—Si3N4, WC tungsten carbide, and zirconium dioxide—ZrO [...] Read more.
This paper presents the results of tribological tests on WE43 and WE54 magnesium alloys with rare earth metals performed in linear reciprocating motion for four different material couples (AISI 316-L steel, silicon nitride—Si3N4, WC tungsten carbide, and zirconium dioxide—ZrO2). Additionally, magnesium alloys were subjected to a complex heat treatment consisting of precipitation hardening combined with a deep cryogenic treatment. The study presents the effect of deep cryogenic treatment combined with precipitation hardening on the tribological properties of WE43 and WE54 alloys. Tribological tests revealed the most advantageous results for the magnesium alloy—AISI 316-L steel friction node. For both alloys tested after heat treatment, a nearly 2-fold reduction in specific wear rate has been achieved. Furthermore, microscopic examinations of the wear track areas and wear products were performed, and the wear mechanisms and types of wear products occurring in linear reciprocating friction were determined. Wear measurements were taken using the 3D profilometric method and compared with the results obtained from calculations performed in accordance with ASTM G133 and ASTM D7755, which were modified to improve the accuracy of the calculation results (the number of measured profiles was increased from four to eight). Appropriately selected calculation methods allow for obtaining reliable tribological test results and enabling the verification of both the most advantageous heat treatment variant and material couple, which results in an increase in the durability of the tested alloys. Full article
(This article belongs to the Special Issue Research on Friction, Wear and Corrosion Properties of Materials)
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<p>An example of surface roughness measurement of WE43 magnesium alloy measured with a Surftest SJ-500 contact profilometer.</p>
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<p>Schematic representation of the experimental set prepared for the tribological test.</p>
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<p>Procedure for measuring the average wear track area in linear reciprocating motion according to modified ASTM G133 and ASTM D7755 standards [<a href="#B12-materials-17-02011" class="html-bibr">12</a>,<a href="#B13-materials-17-02011" class="html-bibr">13</a>].</p>
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<p>Specific wear rate k variations—of WE43 and WE54 magnesium alloys in material couples tested AISI 316-L—(<b>a</b>); ZrO<sub>2</sub>—(<b>b</b>); Si<sub>3</sub>N<sub>4</sub>—(<b>c</b>); WC—(<b>d</b>); in the initial state and after a complex heat treatment process (precipitation hardening—sub-zero treatment).</p>
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<p>Mean stabilized friction coefficient µ<sub>mean</sub> variations—of WE43 and WE54 magnesium alloys in material couples tested AISI 316-L—(<b>a</b>); ZrO<sub>2</sub>—(<b>b</b>); Si<sub>3</sub>N<sub>4</sub>—(<b>c</b>); WC—(<b>d</b>); in the initial state and after a complex heat treatment process (precipitation hardening—sub-zero treatment).</p>
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<p>Three-dimensional isometric images of the cross-sections of the wear track formed as a result of linear reciprocating motion: WE43 alloy in the initial state—(<b>a</b>); WE43 alloy after sub-zero treatment before aging—(<b>b</b>); WE54 alloy—in the initial state—(<b>c</b>); WE54 alloy after sub-zero treatment before and after aging—(<b>d</b>).</p>
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<p>Morphology of WE43 magnesium alloy wear tracks formed in the reciprocating motion of the tested material couples in the initial state (<b>a</b>) and after the complex heat treatment process (precipitation hardening—sub-zero treatment) (<b>b</b>).</p>
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<p>Morphology of WE54 magnesium alloy wear tracks formed in the reciprocating motion of the tested material couples in the initial state (<b>a</b>) and after the complex heat treatment process (precipitation hardening—sub-zero treatment) (<b>b</b>).</p>
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<p>Microanalysis of the chemical composition (EDS) of WE43 alloy wear tracks in the as-delivered condition (<b>a</b>) and after DCT combined with precipitation hardening (<b>b</b>) after a tribological test with an AISI 316-L ball.</p>
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<p>Microanalysis of the chemical composition (EDS) of WE43 alloy wear tracks in the as-delivered condition (<b>a</b>) and after DCT combined with precipitation hardening (<b>b</b>) after a tribological test with an AISI 316-L ball.</p>
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<p>Morphology of wear products of magnesium alloys WE43 and WE54 formed in linear reciprocating motion: ribbon-like strip debris (<b>a</b>,<b>b</b>); lathy-shaped debris (<b>c</b>); dust conglomeration debris (<b>d</b>).</p>
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17 pages, 16150 KiB  
Article
Effect of Deep Cryogenic Aging Treatment on Microstructure and Mechanical Properties of Selective Laser-Melted AlSi10Mg Alloy
by Pengjun Tang, Taiqi Yan, Yu Wu and Haibo Tang
Metals 2024, 14(5), 493; https://doi.org/10.3390/met14050493 - 24 Apr 2024
Cited by 1 | Viewed by 1369
Abstract
Deep cryogenic aging (DCA) is a newly developed heat treatment technique for additive-manufactured metallic materials to reduce residual stress and improve their mechanical properties. In this study, AlSi10Mg alloy samples fabricated by selective laser melting were deep-cryogenic-treated at −160 °C and subsequently aged [...] Read more.
Deep cryogenic aging (DCA) is a newly developed heat treatment technique for additive-manufactured metallic materials to reduce residual stress and improve their mechanical properties. In this study, AlSi10Mg alloy samples fabricated by selective laser melting were deep-cryogenic-treated at −160 °C and subsequently aged at 160 °C. Phase and microstructural analyses were conducted using X-ray diffraction, optical microscopy, scanning electron microscopy, and transmission electron microscopy, while the mechanical properties were evaluated through microhardness and tensile testing at room temperature. The results indicated that the DCA treatment did not have an effect on the morphology of the melt pools. However, it facilitated the formation of atomic clusters and nanoscale Si and β′ phases, as well as accelerating the coarsening of grains and the ripening of the eutectic Si phase. After DCA treatment, the mass fraction of the Si phase experienced an increase from 4.4% to 7.2%. Concurrently, the volume fraction of the precipitated secondary phases elevated to 5.1%. The microhardness was enhanced to 147 HV, and the ultimate tensile strength and yield strength achieved 495 MPa and 345 MPa, respectively, with an elongation of 7.5%. In comparison to the as-built specimen, the microhardness, ultimate tensile strength, and yield strength increased by 11.4%, 3.1%, and 19.0%, respectively. The improvement in mechanical properties is primarily attributed to the Orowan strengthening mechanism induced by the secondary phases. Full article
(This article belongs to the Section Additive Manufacturing)
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<p>The workflow diagram of this research (<b>a</b>); schematic of SLM samples (<b>b</b>).</p>
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<p>Scheme of heat treatment procedure for DC and aging process.</p>
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<p>The XRD patterns of the AB, DA, and DCA samples: 2θ angular range from 20° to 80° (<b>a</b>), diffraction curves of Al (311) peaks (<b>b</b>), partial patterns between 25° and 50° (<b>c</b>), and FWHM results of main diffraction peaks (<b>d</b>).</p>
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<p>The metallographic structures at lower (1) and higher (2) magnification for AB (<b>a1</b>,<b>a2</b>), DA (<b>b1</b>,<b>b2</b>), and DCA (<b>c1</b>,<b>c2</b>) specimens.</p>
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<p>The metallographic structures at lower (1) and higher (2) magnification for AB (<b>a1</b>,<b>a2</b>), DA (<b>b1</b>,<b>b2</b>), and DCA (<b>c1</b>,<b>c2</b>) specimens.</p>
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<p>The SEM morphologies of HAZ (1), CCZ (2), and FCZ (3) in AB (<b>a1</b>–<b>a3</b>), DA (<b>b1</b>–<b>b3</b>), and DCA (<b>c1</b>–<b>c3</b>) specimens.</p>
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<p>The SEM morphologies of HAZ (1), CCZ (2), and FCZ (3) in AB (<b>a1</b>–<b>a3</b>), DA (<b>b1</b>–<b>b3</b>), and DCA (<b>c1</b>–<b>c3</b>) specimens.</p>
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<p>Statistical results of mean diameters and volume fraction of second phases (<b>a</b>); wall thickness and width of cellular eutectic Si network (<b>b</b>).</p>
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<p>The TEM morphologies of SLM AlSi10Mg alloys in AB (<b>a1</b>–<b>a3</b>), DA (<b>b1</b>–<b>b3</b>), and DCA (<b>c1</b>–<b>c3</b>) states.</p>
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<p>The TEM morphologies and corresponding FFT patterns of secondary phases: (<b>a</b>) particle-like β′ and needle-like Si; (<b>b</b>) needle-like and rod-like Si.</p>
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<p>The TEM morphologies and corresponding FFT patterns of secondary phases: (<b>a</b>) particle-like β′ and needle-like Si; (<b>b</b>) needle-like and rod-like Si.</p>
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<p>The microhardness in melt pools of AB, DA, and DCA samples.</p>
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<p>The room temperature tensile properties of AB, DA, and DCA specimens (<b>a</b>), and the plot of yield strength versus elongation for different statuses of SLM AlSi10Mg [<a href="#B1-metals-14-00493" class="html-bibr">1</a>,<a href="#B15-metals-14-00493" class="html-bibr">15</a>,<a href="#B17-metals-14-00493" class="html-bibr">17</a>,<a href="#B23-metals-14-00493" class="html-bibr">23</a>,<a href="#B30-metals-14-00493" class="html-bibr">30</a>,<a href="#B35-metals-14-00493" class="html-bibr">35</a>,<a href="#B36-metals-14-00493" class="html-bibr">36</a>,<a href="#B37-metals-14-00493" class="html-bibr">37</a>] (<b>b</b>).</p>
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<p>The fracture morphologies at lower (1) and higher (2) magnification for AB (<b>a1</b>,<b>a2</b>), DA (<b>b1</b>,<b>b2</b>), and DCA (<b>c1</b>,<b>c2</b>) tensile samples.</p>
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<p>The fracture morphologies at lower (1) and higher (2) magnification for AB (<b>a1</b>,<b>a2</b>), DA (<b>b1</b>,<b>b2</b>), and DCA (<b>c1</b>,<b>c2</b>) tensile samples.</p>
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16 pages, 3827 KiB  
Article
Thermal Characterization and Preclinical Feasibility Verification of an Accessible, Carbon Dioxide-Based Cryotherapy System
by Yixin Hu, Naomi Gordon, Katherine Ogg, Dara L. Kraitchman, Nicholas J. Durr and Bailey Surtees
Bioengineering 2024, 11(4), 391; https://doi.org/10.3390/bioengineering11040391 - 18 Apr 2024
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Abstract
To investigate the potential of an affordable cryotherapy device for the accessible treatment of breast cancer, the performance of a novel carbon dioxide-based device was evaluated through both benchtop testing and an in vivo canine model. This novel device was quantitatively compared to [...] Read more.
To investigate the potential of an affordable cryotherapy device for the accessible treatment of breast cancer, the performance of a novel carbon dioxide-based device was evaluated through both benchtop testing and an in vivo canine model. This novel device was quantitatively compared to a commercial device that utilizes argon gas as the cryogen. The thermal behavior of each device was characterized through calorimetry and by measuring the temperature profiles of iceballs generated in tissue phantoms. A 45 min treatment in a tissue phantom from the carbon dioxide device produced a 1.67 ± 0.06 cm diameter lethal isotherm that was equivalent to a 7 min treatment from the commercial argon-based device, which produced a 1.53 ± 0.15 cm diameter lethal isotherm. An in vivo treatment was performed with the carbon dioxide-based device in one spontaneously occurring canine mammary mass with two standard 10 min freezes. Following cryotherapy, this mass was surgically resected and analyzed for necrosis margins via histopathology. The histopathology margin of necrosis from the in vivo treatment with the carbon dioxide device at 14 days post-cryoablation was 1.57 cm. While carbon dioxide gas has historically been considered an impractical cryogen due to its low working pressure and high boiling point, this study shows that carbon dioxide-based cryotherapy may be equivalent to conventional argon-based cryotherapy in size of the ablation zone in a standard treatment time. The feasibility of the carbon dioxide device demonstrated in this study is an important step towards bringing accessible breast cancer treatment to women in low-resource settings. Full article
(This article belongs to the Special Issue Novel, Low Cost Technologies for Cancer Diagnostics and Therapeutics)
Show Figures

Figure 1

Figure 1
<p>A comparison of the cryoprobe size, shape, and active freezing zone profiles is shown for the two devices. The CO<sub>2</sub> device has a probe diameter of 4.19 mm, while the benchmark argon device has a probe diameter of 1.50 mm.</p>
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<p>Tissue phantom testing setup. The cryoprobe is placed in a custom fixture containing heated ultrasound gel with four thermocouples at fixed radial distances from the probe surface. The ultrasound gel is surrounded by a 37 °C water bath maintained with temperature monitoring and control, simulating the heat load conditions of a body.</p>
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<p>Positions of the four thermocouples. Left: a comparison of the center distance of the thermocouples for the argon and CO<sub>2</sub> probes. Right: a diagram showing the distance of each thermocouple from the probe surface.</p>
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<p>Diagram of the cryotherapy procedure setup. <b>Left</b>: the device is connected to a standard CO<sub>2</sub> tank. <b>Center</b>: the subject is sterilely draped and prepped, and the probe is inserted into the target mass. <b>Right</b>: the device is turned on and an iceball begins to grow around the probe tip inducing necrosis in the mass.</p>
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<p>Temperature data on tissue phantom during the testing period averaged over 10 trials. <span class="html-italic">r</span> represents the distance of the thermocouple from the probe surface.</p>
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<p>Photograph of iceballs generated during testing in the tissue phantom. <b>Left</b>: CO<sub>2</sub> probe; <b>right</b>: benchmark argon probe.</p>
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<p>Means and 95% confidence intervals of the radial temperature distribution from the surface of the probes at the end of the testing period for each device. The red line plots the logarithmic fit of the mean thermocouple data over 10 trials. The gray area represents the 95% confidence interval of the thermocouple data fitted to a logarithmic equation. The distance of the −20 °C isotherm from the surface of the probe with the 95% confidence interval is 6.3 mm (5.9, 6.6) for the CO<sub>2</sub> device and 6.9 mm (6.1, 7.7) for the benchmark argon device.</p>
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<p>Cross-sectional representation of the probe diameters and the mean diameters of the −20 °C isotherms for each probe during testing, extrapolated from the interpolated isotherm radii, assuming radial symmetry around the probe axis. Iceball size is representative.</p>
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<p>Reconstructed photomicrograph from two pieces of the mass containing annotations that show the cryoprobe orientation (black arrow). The region of necrotic tissue is outlined in green, the region of viable tumor tissue in blue, and the maximum length) and width of necrosis relative to the probe track are identified by the yellow and blue dashed lines, respectively. Length measurements do not include regions without tissue between the two pieces.</p>
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<p>Representative regions of the treated mass showing necrotic and viable tumor tissue at 20× magnification. Region I shows necrotic tissue; region II shows the borderline between necrotic and viable tumor tissue; and region III shows viable tumor tissue. The location of each magnified region is noted on the whole slide image (top left).</p>
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