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17 pages, 11121 KiB  
Article
A Study on the Failure Characteristics of Coal–Rock Structures with Different Bursting Liabilities
by Hongyan Li, Shi He, Yunlong Mo, Zhongxue Sun and Lei Li
Processes 2025, 13(3), 652; https://doi.org/10.3390/pr13030652 - 25 Feb 2025
Viewed by 126
Abstract
Research on the deformation and failure behavior of coal is a key scientific issue in the study of coal–rock dynamic disaster prevention technology. It is a critical means to grasp the structural effect of coal–rock deformation and failure behavior to explore the effects [...] Read more.
Research on the deformation and failure behavior of coal is a key scientific issue in the study of coal–rock dynamic disaster prevention technology. It is a critical means to grasp the structural effect of coal–rock deformation and failure behavior to explore the effects of fracture structure on coal–rock deformation and failure behavior. Our experiment on the failure characteristics of coal–rock and the evolution of deformation–fracture structures before the peak stress of coal–rock primarily investigates the influence of fracture structures on its deformation and failure behavior under loading, with a focus on analyzing the size of the primary fractures. The results indicate that the influence of the primary fracture structure on the physical and mechanical properties of coal–rock varies, and the sensitivity of different properties to these structures also differs. Compared to coal–rock without outburst proneness, the fracture structure evolution of coal–rock with strong outburst proneness before failure is more intense and exhibits significant geometric nonlinearity. The size of the fracture that plays the main role in the pre-peak deformation of coal–rock with strong outburst proneness is about one-third of the size of the specimen, and it is about one-fifth of the size of the specimen for coal–rock without outburst proneness. The fracture structure affects the whole deformation process before the failure of coal–rock with strong outburst proneness, but its influence on coal–rock without outburst proneness is gradually reduced with the loading. Full article
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Figure 1

Figure 1
<p>Main test equipment: (<b>a</b>) TAW-2000 electro-hydraulic servo testing machine; (<b>b</b>) LVDT displacement sensor.</p>
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<p>Computer tomography scan imaging system.</p>
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<p>Effect diagram before and after the slice normalizing process: (<b>a</b>) original slice; (<b>b</b>) processed slice.</p>
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<p>The effect diagram of a slice after the filtering process.</p>
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<p>Three-dimensional reconstruction of primary crack structure of coal–rock with strong outburst proneness (Bayangaole Coal Mine).</p>
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<p>Three-dimensional reconstruction of primary crack structure of coal–rock without outburst proneness (Shennanao Coal Mine).</p>
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<p>Fracture structure evolution diagram before peak value: (<b>a</b>) B1; (<b>b</b>) B2; (<b>c</b>) B3; (<b>d</b>) S1.</p>
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<p>Fracture structure evolution diagram before peak value: (<b>a</b>) B1; (<b>b</b>) B2; (<b>c</b>) B3; (<b>d</b>) S1.</p>
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<p>Fracture scale evolution of coal–rock with strong bursting liability (B1 specimen) at different stages.</p>
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<p>Comparison diagram of slices in same position of specimen (XY direction).</p>
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<p>Fracture scale evolution of non-bursting liability coal–rock (S1 specimen) at different stages.</p>
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<p>Physical graphs of coal sample failure: (<b>a</b>) B1; (<b>b</b>) S1.</p>
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<p>Effect of damage degree on internal friction angle.</p>
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22 pages, 4812 KiB  
Article
Mechanical Characterization of a Novel Cyclic Olefin-Based Hot-Melt Adhesive
by Vasco C. M. B. Rodrigues, Ana T. F. Venâncio, Eduardo A. S. Marques, Ricardo J. C. Carbas, Armina Klein, Ejiri Kazuhiro, Björn Nelson and Lucas F. M. da Silva
Materials 2025, 18(4), 855; https://doi.org/10.3390/ma18040855 - 15 Feb 2025
Viewed by 341
Abstract
A novel hot-melt cyclic olefin-based adhesive was designed as a transparent, non-tacky film of amorphous thermoplastic with a unique polymer micro-structure. The aim of the present paper is to assess the mechanical properties of the 0.1 mm thick COP hot-melt adhesive film through [...] Read more.
A novel hot-melt cyclic olefin-based adhesive was designed as a transparent, non-tacky film of amorphous thermoplastic with a unique polymer micro-structure. The aim of the present paper is to assess the mechanical properties of the 0.1 mm thick COP hot-melt adhesive film through adhesive characterizations tests. The glass transition temperature was determined using dynamic mechanical analysis (DMA). For mechanical characterization, bulk and thick adherend shear specimens were manufactured and tested at a quasi-static rate, where at least three specimens were used to calculate the average and standard deviation values. Tensile tests revealed the effects of molecular chain drawing and reorientation before the onset of strain hardening. Thick adherend shear specimens were used to retrieve shear properties. Fracture behaviour was assessed with the double cantilever beam (DCB) test and end-notched flexure (ENF) test, for characterization under modes I and II, respectively. To study the in-joint behaviour, single lap joints (SLJs) of aluminium and carbon fibre-reinforced polymer (CFRP) were manufactured and tested under different temperatures. Results showed a progressive interfacial failure following adhesive plasticization, allowing deformation prior to failure at 8 MPa. An adhesive failure mode was confirmed through scanning electron microscopy (SEM) analysis of aluminium SLJ. The adhesive exhibits tensile properties comparable to existing adhesives, while demonstrating enhanced lap shear strength and a distinctive failure mechanism. These characteristics suggest potential advantages in applications involving heat and pressure across automotive, electronics and structural bonding sectors. Full article
(This article belongs to the Section Advanced Materials Characterization)
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<p>Bulk specimen dimensions according to DIN 53504 standard (dimensions in mm).</p>
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<p>Thick adherend shear joint (dimensions in mm).</p>
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<p>CFRP DCB specimens with loading blocks.</p>
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<p>Manufacturing scheme of SLJs.</p>
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<p>ENF test setup.</p>
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<p>DMA results highlighting the <math display="inline"><semantics> <mi>β</mi> </semantics></math>-relaxation and glass transition temperature.</p>
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<p>Stress–strain engineering curves of the six bulk specimens tested.</p>
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<p>Cold drawing phenomenon observed during the tensile test.</p>
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<p>Engineering and true stress–nominal strain curve.</p>
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<p>Shear stress–strain curve (<b>left</b>) and TAST specimen speckled for DIC analysis and with spring clippers to fix the extensometer (<b>right</b>).</p>
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<p>Reported stretching phenomenon during DCB tests.</p>
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<p>Rotations measured with the sensors and the total rotation curve.</p>
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<p>P-delta and R-curves with a representative opened DCB specimen.</p>
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<p>Rotations measured during one of the tested ENF specimens.</p>
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<p>P-<math display="inline"><semantics> <mi>δ</mi> </semantics></math> and fracture energy curve of the ENF specimen with the rotations displayed in <a href="#materials-18-00855-f014" class="html-fig">Figure 14</a>.</p>
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<p>Lap shear curves for aluminium SLJs tested at room and high (80 °C) temperature.</p>
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<p>Typical failure mode for SLJ using (<b>a</b>) similar aluminium substrates; (<b>b</b>) similar plasma-treated CFRP substrates; (<b>c</b>) dissimilar Al-CFRP substrates.</p>
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<p>Al SLJ recording during the test.</p>
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<p>Aluminium SLJ sample and detail of bonded film (left) and correspondent BSED image from SEM.</p>
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<p>EDS performed at 15 KV on the adhesive film (Z1), aluminium surface (Z2) and a residue present in the adherent surface (Z3).</p>
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<p>EDS performed at 5 KV on the aluminium surface after the peeling of the adhesive film.</p>
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23 pages, 8051 KiB  
Article
Mechanism of Casing Deformation of Shale Gas Platform Wells in Luzhou Block Before Fracturing and Countermeasures for Prevention and Control
by Xiaojun Zhang, Jun Li, Yuxuan Zhao, Wei Cao, Wenbo Zhang, Zongyu Lu and Gonghui Liu
Processes 2025, 13(2), 479; https://doi.org/10.3390/pr13020479 - 10 Feb 2025
Viewed by 451
Abstract
The deep shale gas resources in the Luzhou area of the southern Sichuan Basin are abundant and have been identified as a key replacement field for natural gas development following the medium-to-shallow shale gas fields in Changning and Weiyuan. However, the frequent occurrence [...] Read more.
The deep shale gas resources in the Luzhou area of the southern Sichuan Basin are abundant and have been identified as a key replacement field for natural gas development following the medium-to-shallow shale gas fields in Changning and Weiyuan. However, the frequent occurrence of “pre-deformation without fracturing” in horizontal wells has significantly restricted large-scale production. In this study, the Lu203 and Yang101 well areas were analyzed to investigate the characteristics of casing deformation and the correlation with faults and natural fractures (fracture systems). A numerical model of multi-stage fracturing for platform wells was established based on microseismic event data, and the effects of fracturing on the stress and casing stress of adjacent wells were simulated and analyzed. The results indicate that the development of fracture systems is the primary cause of the “pre-deformation without fracturing” phenomenon. The propagation of fracturing fluid through fractures significantly increases the stress and loading around adjacent wells, causing casing stress to exceed its yield strength. To mitigate this issue, a method involving the injection of approximately 10 MPa of internal casing pressure into unfractured wells was proposed, effectively reducing the risk of casing deformation and failure. This provides technical support for the efficient development of deep shale gas. Full article
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Figure 1
<p>Statistical results of casing deformation wells in the Luzhou block.</p>
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<p>The correlation between casing deformation points and natural fractures in the Luzhou block. (<b>a</b>) Relationship between casing deformation points and natural fracture distances. (<b>b</b>) Relationship between casing deformation points and natural fracture angles.</p>
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<p>Relationship between fracture distribution and casing deformation point of platforms H1–H4 in the Lu203 well area.</p>
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<p>Schematic of casing deformation before fracturing in platform wells.</p>
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<p>Distribution characteristics of microseismic signals from 1 to 10 fracturing of Well X-6 in the Lu203 well area.</p>
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<p>Simplified processing map of microseismic event points for the X Platform.</p>
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<p>Finite element numerical modeling of platform well fracturing. (<b>a</b>) Finite element model. (<b>b</b>) Localized view of casing-cement formation assemblage. (<b>c</b>) Model cross-section. (<b>d</b>) Fracturing region.</p>
Full article ">Figure 7 Cont.
<p>Finite element numerical modeling of platform well fracturing. (<b>a</b>) Finite element model. (<b>b</b>) Localized view of casing-cement formation assemblage. (<b>c</b>) Model cross-section. (<b>d</b>) Fracturing region.</p>
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<p>Characterization of pore pressure variations around unfractured wells. (<b>a</b>) Well X-4. (<b>b</b>) Well X-5.</p>
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<p>Characterization of maximum horizontal principal stress variations around unfractured wells. (<b>a</b>) Well X-4. (<b>b</b>) Well X-5.</p>
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<p>Characterization of casing stress changes in Well X-6. (<b>a</b>) Before fracturing. (<b>b</b>) After fracturing. (<b>c</b>) Casing stress changes at different fracturing stages.</p>
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<p>Characteristics of casing stress changes in Well X-4 at different fracturing stages.</p>
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<p>Characteristics of casing stress change in Well X-5 at different fracturing stages.</p>
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<p>Characteristics of casing circumferential stress distribution at different locations in Well X-5.</p>
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<p>Deformation displacement of Well X-5 casing in the direction of the maximum principal stress at different fracturing stages.</p>
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<p>Interpreted results of multi-arm well log measurement at 4591.7–4593.28 m in Well X-5.</p>
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<p>Prevention and control schematic.</p>
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<p>Characterization of casing stress changes in unfractured wells under pre-injection of internal pressure of 20 MPa.</p>
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<p>Characteristics of casing stress changes in unfractured wells under different internal pressure conditions.</p>
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40 pages, 11072 KiB  
Article
An Approach to Evaluate the Fatigue Life of the Material of Liquefied Gases’ Vessels Based on the Time Dependence of Acoustic Emission Parameters: Part 1
by Oleg G. Perveitalov and Viktor V. Nosov
Metals 2025, 15(2), 148; https://doi.org/10.3390/met15020148 - 31 Jan 2025
Viewed by 536
Abstract
In the first part of this article devoted to the assessment of the fatigue life of structural steels at low temperatures, a study was conducted on the effect of pre-cycling in a low-cycle fatigue mode on the time dependences of acoustic emission parameters. [...] Read more.
In the first part of this article devoted to the assessment of the fatigue life of structural steels at low temperatures, a study was conducted on the effect of pre-cycling in a low-cycle fatigue mode on the time dependences of acoustic emission parameters. Commonly used St-3 steel was tested at −60 °C with varying durabilities, after which it was fractured once during static tests. The multilevel acoustic model used made it possible to estimate the structural parameter γ at the stage of elastoplastic deformation. The stage of active development of microcracks and their coalescence corresponds to a homogeneous fracture with stable acoustic emission characteristics (signal duration, amplitude variation coefficient, etc.). It was shown that regardless of the maximum voltage (460, 480, and 500 MPa) in the cycle and the operating times of up to 0.3, 0.5, and 0.7, the structural parameter remains within the known limits. The parameters of the Weibull law distribution and the logarithmically normal distribution for the coefficient γ were obtained, theoretical and calculated fatigue curves were plotted, and a method was proposed for evaluating the number of cycles before fracture under irregular loading conditions in the real operation of pressure vessels based on the “rainflow” cycles counting method. Full article
(This article belongs to the Special Issue Fatigue Assessment of Metals)
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Figure 1
<p>The dependence of durability on stress for various loading modes for St-3 steel (according to [<a href="#B31-metals-15-00148" class="html-bibr">31</a>]).</p>
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<p>Geometric dimensions of the low-cycle fatigue test specimen.</p>
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<p>Test equipment: (<b>a</b>) Instron 8802 250 kN servo-hydraulic machine and Zwick/Roell BW91250 thermal camera; (<b>b</b>) arrangement of waveguides on the specimen.</p>
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<p>Specimen location in a thermal chamber with a fixed Instron DIN 2620-604 dynamic deformation sensor (extensometer).</p>
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<p>Cycle scheme during fatigue loading.</p>
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<p>A-Line work screen for processing AE signals during Specimen VII tests. Red color—1 channel; green color—2 channel.</p>
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<p>Time dependences of the cumulative AE count (black points) and stress changes (red points) during single tensile tests after various degrees of operation at 213 K: (<b>a</b>) without operation (Specimen I); (<b>b</b>) <math display="inline"><semantics> <mrow> <mrow> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>i</mi> </mrow> </msub> </mrow> <mo>/</mo> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>f</mi> </mrow> </msub> </mrow> </mrow> <mo>=</mo> <mn>0.3</mn> </mrow> </semantics></math> at <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>σ</mi> </mrow> <mrow> <mi>m</mi> <mi>a</mi> <mi>x</mi> </mrow> </msub> <mo>=</mo> <mn>460</mn> <mtext> </mtext> <mi mathvariant="normal">M</mi> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">a</mi> </mrow> </semantics></math> (Specimen VI); (<b>c</b>) <math display="inline"><semantics> <mrow> <mrow> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>i</mi> </mrow> </msub> </mrow> <mo>/</mo> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>f</mi> </mrow> </msub> </mrow> </mrow> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math> at <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>σ</mi> </mrow> <mrow> <mi>m</mi> <mi>a</mi> <mi>x</mi> </mrow> </msub> <mo>=</mo> <mn>480</mn> <mtext> </mtext> <mi mathvariant="normal">M</mi> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">a</mi> </mrow> </semantics></math> (Specimen VII); and (<b>d</b>) <math display="inline"><semantics> <mrow> <mrow> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>i</mi> </mrow> </msub> </mrow> <mo>/</mo> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>f</mi> </mrow> </msub> </mrow> </mrow> <mo>=</mo> <mn>0.7</mn> </mrow> </semantics></math> at <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>σ</mi> </mrow> <mrow> <mi>m</mi> <mi>a</mi> <mi>x</mi> </mrow> </msub> <mo>=</mo> <mn>500</mn> <mtext> </mtext> <mi mathvariant="normal">M</mi> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">a</mi> </mrow> </semantics></math> (Specimen VIII).</p>
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<p>Time dependence of the logarithm of the cumulative AE count: (<b>a</b>) without pre-fatigue (Specimen I); (<b>b</b>) <math display="inline"><semantics> <mrow> <mrow> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>i</mi> </mrow> </msub> </mrow> <mo>/</mo> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>f</mi> </mrow> </msub> </mrow> </mrow> <mo>=</mo> <mn>0.3</mn> </mrow> </semantics></math> at <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>σ</mi> </mrow> <mrow> <mi>m</mi> <mi>a</mi> <mi>x</mi> </mrow> </msub> <mo>=</mo> <mn>460</mn> <mtext> </mtext> <mi mathvariant="normal">M</mi> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">a</mi> </mrow> </semantics></math> (Specimen VI); (<b>c</b>) <math display="inline"><semantics> <mrow> <mrow> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>i</mi> </mrow> </msub> </mrow> <mo>/</mo> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>f</mi> </mrow> </msub> </mrow> </mrow> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math> at <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>σ</mi> </mrow> <mrow> <mi>m</mi> <mi>a</mi> <mi>x</mi> </mrow> </msub> <mo>=</mo> <mn>480</mn> <mtext> </mtext> <mi mathvariant="normal">M</mi> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">a</mi> </mrow> </semantics></math> (Specimen VII); and (<b>d</b>) <math display="inline"><semantics> <mrow> <mrow> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>i</mi> </mrow> </msub> </mrow> <mo>/</mo> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>f</mi> </mrow> </msub> </mrow> </mrow> <mo>=</mo> <mn>0.7</mn> </mrow> </semantics></math> at <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>σ</mi> </mrow> <mrow> <mi>m</mi> <mi>a</mi> <mi>x</mi> </mrow> </msub> <mo>=</mo> <mn>500</mn> <mtext> </mtext> <mi mathvariant="normal">M</mi> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">a</mi> </mrow> </semantics></math> (Specimen VIII).</p>
Full article ">Figure 8 Cont.
<p>Time dependence of the logarithm of the cumulative AE count: (<b>a</b>) without pre-fatigue (Specimen I); (<b>b</b>) <math display="inline"><semantics> <mrow> <mrow> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>i</mi> </mrow> </msub> </mrow> <mo>/</mo> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>f</mi> </mrow> </msub> </mrow> </mrow> <mo>=</mo> <mn>0.3</mn> </mrow> </semantics></math> at <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>σ</mi> </mrow> <mrow> <mi>m</mi> <mi>a</mi> <mi>x</mi> </mrow> </msub> <mo>=</mo> <mn>460</mn> <mtext> </mtext> <mi mathvariant="normal">M</mi> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">a</mi> </mrow> </semantics></math> (Specimen VI); (<b>c</b>) <math display="inline"><semantics> <mrow> <mrow> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>i</mi> </mrow> </msub> </mrow> <mo>/</mo> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>f</mi> </mrow> </msub> </mrow> </mrow> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math> at <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>σ</mi> </mrow> <mrow> <mi>m</mi> <mi>a</mi> <mi>x</mi> </mrow> </msub> <mo>=</mo> <mn>480</mn> <mtext> </mtext> <mi mathvariant="normal">M</mi> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">a</mi> </mrow> </semantics></math> (Specimen VII); and (<b>d</b>) <math display="inline"><semantics> <mrow> <mrow> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>i</mi> </mrow> </msub> </mrow> <mo>/</mo> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>f</mi> </mrow> </msub> </mrow> </mrow> <mo>=</mo> <mn>0.7</mn> </mrow> </semantics></math> at <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>σ</mi> </mrow> <mrow> <mi>m</mi> <mi>a</mi> <mi>x</mi> </mrow> </msub> <mo>=</mo> <mn>500</mn> <mtext> </mtext> <mi mathvariant="normal">M</mi> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">a</mi> </mrow> </semantics></math> (Specimen VIII).</p>
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<p>AE features for determining the start and end times of the uniform fracture stage for specimen VII (<math display="inline"><semantics> <mrow> <mrow> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>i</mi> </mrow> </msub> </mrow> <mo>/</mo> <mrow> <msub> <mrow> <mi>N</mi> </mrow> <mrow> <mi>f</mi> </mrow> </msub> </mrow> </mrow> <mo>=</mo> <mn>0.7</mn> </mrow> </semantics></math> at <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>σ</mi> </mrow> <mrow> <mi>m</mi> <mi>a</mi> <mi>x</mi> </mrow> </msub> <mo>=</mo> <mn>500</mn> <mtext> </mtext> <mi mathvariant="normal">M</mi> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">a</mi> </mrow> </semantics></math>): (<b>a</b>) time dependence of the signal overlap coefficient; (<b>b</b>) time dependence of the amplitude variation coefficient.</p>
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<p>Photo of specimens that underwent static tensile and fatigue tests: specimens I, II, and specimens IV–XI.</p>
Full article ">Figure 11
<p>Results of fatigue life calculations based on low-temperature AE testing: (<b>a</b>) calculated and experimental fatigue life values; (<b>b</b>) fatigue curve of St-3 steel at low temperatures for similar specimens according to Strizhalo [<a href="#B51-metals-15-00148" class="html-bibr">51</a>].</p>
Full article ">Figure 12
<p>Results of acoustic emission tests for single static fracture of standard specimens after various levels of fatigue accumulation: (<b>a</b>) time dependencies of the cumulative AE count for specimens after an accumulation of 0.3, 0.5, and 0.7 of the life and in the initial state during static tests and (<b>b</b>) time dependencies of the logarithm of the cumulative AE count and stress–strain curves (steel 20) [<a href="#B58-metals-15-00148" class="html-bibr">58</a>]; (<b>c</b>) time dependencies of the cumulative AE count for specimens after an accumulation of 0.3, 0.5, and 0.7 of the life and in the initial state during static tests and (<b>d</b>) time dependencies of the logarithm of the cumulative AE count and stress–strain curves (low-carbon steel 20) [<a href="#B55-metals-15-00148" class="html-bibr">55</a>]; (<b>e</b>) time dependencies of the cumulative AE count for specimens after an accumulation of 0.3, 0.5, and 0.7 of the life, in the initial state and a tensile specimen during static tests and (<b>f</b>) time dependencies of the logarithm of the cumulative AE count and stress–strain curves (steel 15Kh2GMF) [<a href="#B53-metals-15-00148" class="html-bibr">53</a>].</p>
Full article ">Figure 12 Cont.
<p>Results of acoustic emission tests for single static fracture of standard specimens after various levels of fatigue accumulation: (<b>a</b>) time dependencies of the cumulative AE count for specimens after an accumulation of 0.3, 0.5, and 0.7 of the life and in the initial state during static tests and (<b>b</b>) time dependencies of the logarithm of the cumulative AE count and stress–strain curves (steel 20) [<a href="#B58-metals-15-00148" class="html-bibr">58</a>]; (<b>c</b>) time dependencies of the cumulative AE count for specimens after an accumulation of 0.3, 0.5, and 0.7 of the life and in the initial state during static tests and (<b>d</b>) time dependencies of the logarithm of the cumulative AE count and stress–strain curves (low-carbon steel 20) [<a href="#B55-metals-15-00148" class="html-bibr">55</a>]; (<b>e</b>) time dependencies of the cumulative AE count for specimens after an accumulation of 0.3, 0.5, and 0.7 of the life, in the initial state and a tensile specimen during static tests and (<b>f</b>) time dependencies of the logarithm of the cumulative AE count and stress–strain curves (steel 15Kh2GMF) [<a href="#B53-metals-15-00148" class="html-bibr">53</a>].</p>
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<p>Results of acoustic emission tests for single static fracture of standard specimens after various levels of fatigue accumulation: (<b>a</b>) time dependencies of the cumulative AE count for specimens after an accumulation of 0.3, 0.5, and 0.7 of the life and in the initial state during static tests and (<b>b</b>) time dependencies of the logarithm of the cumulative AE count and stress–strain curves (steel 20) [<a href="#B58-metals-15-00148" class="html-bibr">58</a>]; (<b>c</b>) time dependencies of the cumulative AE count for specimens after an accumulation of 0.3, 0.5, and 0.7 of the life and in the initial state during static tests and (<b>d</b>) time dependencies of the logarithm of the cumulative AE count and stress–strain curves (low-carbon steel 20) [<a href="#B55-metals-15-00148" class="html-bibr">55</a>]; (<b>e</b>) time dependencies of the cumulative AE count for specimens after an accumulation of 0.3, 0.5, and 0.7 of the life, in the initial state and a tensile specimen during static tests and (<b>f</b>) time dependencies of the logarithm of the cumulative AE count and stress–strain curves (steel 15Kh2GMF) [<a href="#B53-metals-15-00148" class="html-bibr">53</a>].</p>
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<p>Fatigue curves for the experimental materials with marked points of the calculated fatigue life: (<b>a</b>) steel 20 with preliminary cycling at 390 MPa; (<b>b</b>) steel 20 with preliminary loading at 330 MPa; and (<b>c</b>) steel 15Kh2GMF with preliminary loading at 800 MPa.</p>
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<p>Fatigue curves for the experimental materials with marked points of the calculated fatigue life: (<b>a</b>) steel 20 with preliminary cycling at 390 MPa; (<b>b</b>) steel 20 with preliminary loading at 330 MPa; and (<b>c</b>) steel 15Kh2GMF with preliminary loading at 800 MPa.</p>
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<p>Distribution of the structural parameter <math display="inline"><semantics> <mrow> <mi>γ</mi> </mrow> </semantics></math> during uniform fracture of specimens VI, VII, and VIII. (<b>a</b>) Weibull distribution; (<b>b</b>) log-normal distribution.</p>
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<p>Comparison of experimental and calculated values of cumulative AE count based on numerical simulation data.</p>
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<p>Results of modeling the stress state of the gas receiver under operating conditions: (<b>a</b>) stress distribution over the object’s surface and maximum stresses in the area near the flange (as a natural stress concentrator); (<b>b</b>) results of the residual fatigue life calculation based on the low-cycle fatigue criterion using the Manson–Coffin model, taking into account the accumulation of plastic deformation.</p>
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<p>Example diagram for determining the range of acting stresses in the concentrator—the source of AE signals: (<b>a</b>) logarithm of the cumulative AE count and the pressure increase graph during hydraulic testing of the vessel [<a href="#B70-metals-15-00148" class="html-bibr">70</a>]; (<b>b</b>) logarithm of the cumulative count and stress during the testing of laboratory specimens from the pressure vessel material (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>t</mi> </mrow> <mrow> <mn>1</mn> </mrow> </msub> </mrow> </semantics></math>—time moment of the beginning of the uniform microcracking stage).</p>
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<p>Operational data for converting pressure drop cycles in a liquid ethylene storage tank 47D01 into a fatigue curve relationship – pressure drop oscillogram over the course of a year.</p>
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<p>Simulation of the operational pressure drop process using laboratory AE testing of standard specimens and Comsol Multiphysics 5.6 software: (<b>a</b>) a graph of pressure changes in the tank during the year, modeled using the software; (<b>b</b>) stress–strain state of a standard specimen for low-cycle fatigue.</p>
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<p>Matrix histograms of the distribution of loading blocks of a real vessel (<b>a</b>) by stress amplitude <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>σ</mi> </mrow> <mo stretchy="false">^</mo> </mover> </mrow> </semantics></math> and mean cycle stress <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>σ</mi> </mrow> <mo stretchy="false">¯</mo> </mover> </mrow> </semantics></math> and (<b>b</b>) by relative contribution to damage accumulation.</p>
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<p>Flowchart of the method implementation.</p>
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17 pages, 7903 KiB  
Article
Analysis of Crack Initiation in Hot Forging Process with the Support of the Digital Image Correlation System
by Łukasz Lisiecki, Paulina Lisiecka-Graca and Nikolaos E. Karkalos
Appl. Sci. 2025, 15(1), 408; https://doi.org/10.3390/app15010408 - 4 Jan 2025
Viewed by 630
Abstract
The limits of plastic deformation without failure are considered to be a measure of formability and can be estimated by the standard tests. However, the mechanical states observed during commonly used compression tests are similar to those observed in many bulk deformation processes, [...] Read more.
The limits of plastic deformation without failure are considered to be a measure of formability and can be estimated by the standard tests. However, the mechanical states observed during commonly used compression tests are similar to those observed in many bulk deformation processes, with an additional advantage of those tests having the possibility of applying large deformations without the risk of the appearance of necking (in tension) or material reorientation (in torsion). Thus, this study presents the results of modified compression tests under conditions of a real forging process, since knowledge of the geometrical parameters of the tools and samples makes it possible to determine the areas of stress concentration which contribute to the formation of controlled cracks. The digital image correlation system (DIC) was used to analyze the deformation parameters that lead to achieving the critical values of fracture criterion; simulations were additionally performed to confirm the reliability of predicting the location and the critical moment just before failure in the forging process under consideration. After the accuracy of the model was verified, this approach was applied to a case of backward extrusion, also correctly predicting the locations with high probability of fracture. Full article
(This article belongs to the Special Issue Advanced Manufacturing Processes: Technologies and Applications)
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<p>Experimental laboratory research: (<b>a</b>) the initial sample, (<b>b</b>) laboratory hydraulic press, (<b>c</b>) DIC system coupled with a laboratory press.</p>
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<p>The DIC Q400 system components and schematic diagram of measurement before and after deformation.</p>
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<p>Stress–strain curves for the analyzed materials tested at 320 °C and images of the initial microstructures.</p>
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<p>The system of tools used for laboratory tests: (<b>a</b>) model of the tools, (<b>b</b>) tools in the working area of hydraulic press, (<b>c</b>–<b>f</b>) different stages of the test.</p>
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<p>Different sample positions in relation to the DIC cameras during deformation of cuboidal samples.</p>
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<p>Finite element mesh distribution on the tools and sample models before (<b>a</b>) and after (<b>b</b>) modified compression test simulation.</p>
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<p>The results of the compression test of samples with: (<b>a</b>–<b>d</b>) the side edge facing the camera—Grade A, (<b>e</b>–<b>h</b>) the side wall facing towards the camera—Grade B.</p>
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<p>Comparison of the deformation process parameters under the experimental conditions with those calculated in the computer simulation: (<b>a</b>) change in load with time during compression for Grade A and B, (<b>b</b>) principal strain change at the point of fracture—Grade A and B.</p>
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<p>Distribution of fracture criteria on sample surfaces: (<b>a</b>,<b>b</b>) grade A; (<b>c</b>,<b>d</b>) grade B; (<b>a</b>,<b>c</b>) Rice and Tracey fracture criterion; (<b>b</b>,<b>d</b>) Cockcroft and Latham fracture criterion.</p>
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<p>Examples of material fracture after backward extrusion process: (<b>a</b>–<b>c</b>) different localization of defects (marked by red circles).</p>
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<p>Change in product shape during backward extrusion: (<b>a</b>–<b>e</b>) subsequent stages of the process.</p>
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<p>Analysis of the distribution of parameters during backward extrusion: (<b>a</b>–<b>c</b>) change in the Cockcroft–Latham fracture criterion value during extrusion, (<b>d</b>) distribution of the principal strain, (<b>e</b>) distribution of the effective strain.</p>
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<p>Changes in the values of selected parameters at characteristic points located on the inner and outer surfaces of the sample and the extruded product: (<b>a</b>) values of the Cockcroft–Latham fracture criterion on the sample surfaces, (<b>b</b>) values of the principal strain on the sample surfaces, (<b>c</b>) comparison of the Cockcroft–Latham fracture criterion and the principal strain at the point of their maximum concentration on the surface of the extruded product.</p>
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<p>Changes in the values of selected parameters at characteristic points located on the inner and outer surfaces of the sample and the extruded product: (<b>a</b>) values of the Cockcroft–Latham fracture criterion on the sample surfaces, (<b>b</b>) values of the principal strain on the sample surfaces, (<b>c</b>) comparison of the Cockcroft–Latham fracture criterion and the principal strain at the point of their maximum concentration on the surface of the extruded product.</p>
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16 pages, 5153 KiB  
Article
Small Surface Fatigue Crack Behaviors of Cr-Mo Steel AISI4137
by Seung-Hoon Nahm, Sang-Koo Jeon, Dong-Kyun Kim, Min-Soo Suh and Chang-Min Suh
Crystals 2025, 15(1), 45; https://doi.org/10.3390/cryst15010045 - 31 Dec 2024
Viewed by 416
Abstract
Costs are increasing due to the addition of alloying elements such as V, W, and Mo to prevent damage to Cr-Mo steel for fastening bolts, but field tests have shown that it is not an appropriate solution for improving physical properties through heat [...] Read more.
Costs are increasing due to the addition of alloying elements such as V, W, and Mo to prevent damage to Cr-Mo steel for fastening bolts, but field tests have shown that it is not an appropriate solution for improving physical properties through heat treatment. In this study, the characteristics of fatigue cracks using Cr-Mo steel for fastening bolts before and after UNSM (ultrasonic nanocrystal surface modification) treatment were studied using fracture mechanics and fracture analysis methods. Specifically, using untreated and UNSM-treated materials: (1) the characteristics of small surface fatigue cracks existing on the surface, and (2) the surface fatigue cracks in the depth direction were observed and analyzed. The microstructure of Cr-Mo steel was refined by severe plastic deformation (SPD) from the surface to a depth of about 100 μm according to the static load of UNSM, and the fatigue limit increased by 30% as a large compressive residual stress was formed. Additionally, like the untreated materials, fisheye cracks did not occur in UNSM-treated materials, even when inclusions were present, and all specimens fractured while forming surface cracks. Accordingly, one or more of the multiple small surface fatigue cracks (MSFC) grew and developed into a major crack that determines the fatigue life, and a major ridge was formed among the many micro-ridges in the internal direction. In other words, this major crack grew and developed a major ridge in the internal direction, determining the lifespan of the test specimen. Full article
(This article belongs to the Special Issue Microstructural Characterization and Property Analysis of Alloys)
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<p>(<b>a</b>) UNSM system, (<b>b</b>) the traces of 3D (x, y, z) surfaces using an atomic force microscope (AFM) after UNSM treatment.</p>
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<p>(<b>A</b>). Configuration of fatigue specimen (unit; mm) and (<b>B</b>) cantilever-type rotary bending fatigue testing machine. (a) motor, (b) spindle, (c) specimens, (d) sensor, (e) bearing and spring, (f) weight, (g) counter.</p>
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<p>Photos of changes in microstructure “before and after UNSM” observed at 100× magnification during UNSM treatment. (<b>a</b>) before UNSM, (<b>b</b>) after UNSM 100N. (<b>c</b>) The traces of 3D (x = 10 μm, y = 10 μm, z = 400 nm) forging and (<b>d</b>) the traces of 2D (x = 0.6 μm, y = 0.16 μm) forging using an atomic force microscope after UNSM 100N treatment.</p>
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<p>Photos of changes in microstructure “before and after UNSM” observed at 100× magnification during UNSM treatment. (<b>a</b>) before UNSM, (<b>b</b>) after UNSM 100N. (<b>c</b>) The traces of 3D (x = 10 μm, y = 10 μm, z = 400 nm) forging and (<b>d</b>) the traces of 2D (x = 0.6 μm, y = 0.16 μm) forging using an atomic force microscope after UNSM 100N treatment.</p>
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<p>Enlarged images of the surface condition of the specimen before (<b>a</b>) and after (<b>b</b>) UNSM treatment in 3D traces in a relatively large area (x = 450 μm, y = 450 μm, z = 10 μm) using an atomic force microscope (AFM).</p>
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<p>(<b>a</b>). Distribution of micro Vickers hardness from surface before and after UNSM treatment of AISI4137. (<b>b</b>) shows data comparing the change in compressive residual stress of AISI4137 along the depth direction.</p>
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<p>(<b>a</b>) shows the S-N diagram of Sakai’s SCM435 [<a href="#B13-crystals-15-00045" class="html-bibr">13</a>] as “Ground” with square marks and the results of this study with circular marks and compares them at the same time. (<b>b</b>) The S-N data for AISI4137 material treated with UNSM under a static load of 40N was compared to the “Ground” data (green line) in the diamond marks and the red line. (<b>c</b>) The S-N data for Cr-Mo steel treated with UNSM under a static load of 70 N was compared to the “Ground” data (green line) in the circular marks and the black line. (<b>d</b>) shows a simultaneous comparison of all S-N diagram data for Cr-Mo steel before and after UNSM treatment.</p>
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<p>(<b>a</b>) A photo taken by mosaic picture of a small surface fatigue crack obtained by replica film under UNSM-70N treatment at 670 MPa, N = 2.14 × 10<sup>5</sup> (N/N<sub>f</sub> = 93%, N<sub>f</sub> =2.3 × 10<sup>5</sup>). The small surface fatigue cracks grew and coalesced to become the major crack that determined fatigue life. (<b>b</b>,<b>c</b>) were SEM photos taken of the fracture surface. As shown by the arrow in (<b>a</b>), a small surface fatigue crack occurs as a single crack, and the growth process is sketched with dotted line in (<b>b</b>). (<b>c</b>) is a photo taken at 100× of the origin of the surface crack initiation site of (<b>b</b>).</p>
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<p>(<b>a</b>) is an SEM photograph taken at 20× magnification of the fractured surface of UNSM-100N-treated material at 675 MPa and N<sub>f</sub> = 3.1 × 10<sup>5</sup>. The three arrows in the picture sketch the process of surface crack formation, growth, coalescence, and fracture with dotted lines. (<b>b</b>) is a photograph taken at 500× magnification of the origin of S1, and inclusions are indicated by small red circles at the origin of the surface crack. It can be seen that the surface grows and coalesces with adjacent micro-cracks. Additionally, micro-cracks inside the material form micro-ridges, and the process of increasing depth in the inner direction is repeated.</p>
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<p>(<b>a</b>) is an SEM photograph taken at 20× magnification of the fracture surface at 800 MPa and N<sub>f</sub> = 2.6 × 10<sup>4</sup> in UNSM-100N-treated material. (<b>b</b>) is a photograph taken at 500× magnification of the origin of surface crack S1. Inclusions are indicated by a red circle at the origin of the small surface fatigue crack.</p>
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<p>(<b>A</b>) At the grain boundary (GB), which is vulnerable to tensile stress, a persistent slip band (PSB) appears, as shown in the figure, and gradually develops into a major crack that determines the life of the specimen (mild steel, 220 MPa, N<sub>f</sub> = 4.8 × 10<sup>5</sup>). The crack grows both on the surface (Figure (<b>a</b>–<b>c</b>,<b>f</b>–<b>i</b>)) and in the depth (<a href="#crystals-15-00045-f008" class="html-fig">Figure 8</a>b and <a href="#crystals-15-00045-f009" class="html-fig">Figure 9</a>b) direction. (<b>B</b>) These data visualize the behavior of micro-surface fatigue cracks in a photograph connected using the mosaic method on tracing paper. The state in which many fatigue cracks appear on the surface and coalesce is shown in <a href="#crystals-15-00045-f010" class="html-fig">Figure 10</a>B. Among these many micro-surface cracks, one is a major crack and determines the fatigue life of the specimen (mild steel, 333 MPa, N<sub>f</sub> = 1.17 × 10<sup>5</sup>), N/N<sub>f</sub> = 0.17 (<b>a</b>), 0.43 (<b>b</b>), 0.85 (<b>c</b>), and 0.97 (<b>d</b>) [<a href="#B17-crystals-15-00045" class="html-bibr">17</a>,<a href="#B18-crystals-15-00045" class="html-bibr">18</a>,<a href="#B19-crystals-15-00045" class="html-bibr">19</a>,<a href="#B20-crystals-15-00045" class="html-bibr">20</a>].</p>
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<p>(<b>a</b>) Comparison curve according to the growth and cycle ratio of the surface fatigue crack length on a small circular artificial notch material with a surface and depth of 0.1 mm in medium carbon steel [<a href="#B21-crystals-15-00045" class="html-bibr">21</a>]. (<b>b</b>) is a sketch tracing the morphology of micro-surface fatigue cracks at a stage (cycle ratio about 32%) prior to the eight dashed lines in (<b>c</b>). (<b>c</b>) is a sketch of the shape of micro surface fatigue cracks and micro-ridges in the depth direction by rotating <a href="#crystals-15-00045-f008" class="html-fig">Figure 8</a>b by 90 degrees, which corresponds to cycle ratio about 40%.</p>
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21 pages, 7674 KiB  
Article
Fatigue Experiment and Failure Mechanism Analysis of Aircraft Titanium Alloy Wing–Body Connection Joint
by Xianmin Chen, Shanshan Li, Yuanbo Liang, Shuo Wang, Liang Yan and Shichang Du
Sensors 2025, 25(1), 150; https://doi.org/10.3390/s25010150 - 30 Dec 2024
Viewed by 643
Abstract
Taking the titanium alloy wing–body connection joint at the rear beam of a certain type of aircraft as the research object, this study analyzed the failure mechanism and verified the structural safety of the wing–body connection joint under actual flight loads. Firstly, this [...] Read more.
Taking the titanium alloy wing–body connection joint at the rear beam of a certain type of aircraft as the research object, this study analyzed the failure mechanism and verified the structural safety of the wing–body connection joint under actual flight loads. Firstly, this study verified the validity of the loading system and the measuring system in the test system through the pre-test, and the repeatability of the test was analyzed for error to ensure the accuracy of the experimental data. Then, the test piece was subjected to 400,000 random load tests of flight takeoffs and landings, 100,000 Class A load tests, and ground–air–ground load tests, and the test piece fractured under the ground–air–ground load tests. Lastly, the mechanism analysis and structural safety verification of the fatigue fracture of the joints were carried out by using a stereo microscope and scanning electron microscope. The results show that fretting fatigue is the main driving force for crack initiation, and the crack shows significant fatigue damage characteristics in the stable growth stage and follows Paris’ law. Entering the final fracture region, the joint mainly experienced ductile fracture, with typical plastic deformation features such as dimples and tear ridges before fracture. The fatigue crack growth behavior of the joint was quantitatively analyzed using Paris’ law, and the calculated crack growth period life was 207,374 loadings. This result proves that the crack initiation life accounts for 95.19% of the full life cycle, which is much higher than the design requirement of 400,000 landings and takeoffs, indicating that the structural design of this test piece is on the conservative side and meets the requirements of aircraft operational safety. This research is of great significance in improving the safety and reliability of aircraft structures. Full article
(This article belongs to the Special Issue Applications of Manufacturing and Measurement Sensors: 2nd Edition)
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<p>The diagram of the experimental piece configuration and the main dimensions.</p>
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<p>The diagram of the typical load spectrum.</p>
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<p>The diagram of the experimental support scheme.</p>
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<p>Schematic diagram of attaching strain gauges on pull rod.</p>
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<p>Fatigue experiment scheme and inspection interval flow chart.</p>
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<p>Symmetry analysis of strain measurement data.</p>
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<p>Repeatability analysis of strain measurement data.</p>
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<p>Diagram of the joint fatigue fracture.</p>
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<p>Diagram of crack location and macroscopic shape of the experimental piece. (<b>a</b>) a side view of the wing-fuselage connector, with a stereoscopic microscope diagram showing the fracture location on the right; (<b>b</b>) another side view of the wing-fuselage connector (the back of (<b>a</b>)), with a stereoscopic microscope diagram showing the fracture location on the right; (<b>c</b>) a top view of the wing-fuselage connector.</p>
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<p>Diagram of the direction of loading force and crack direction. (<b>a</b>) physical picture of the experimental piece; (<b>b</b>) plan view of the experimental piece.</p>
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<p>Macroscopic morphology of the fracture of the experimental piece.</p>
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<p>SEM electron micrograph of the fracture.</p>
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<p>SEM electron micrograph of the fatigue source region. (<b>a</b>) SEM electron microscope photo at 100 times; (<b>b</b>) SEM electron microscope photo at 200 times; (<b>c</b>) SEM electron microscope photo at 500 times; (<b>d</b>) SEM electron microscope photo at 1000 times.</p>
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<p>SEM electron micrograph of fatigue growth region. (<b>a</b>) SEM electron microscope photo at 50 times; (<b>b</b>) SEM electron microscope photo at 100 times; (<b>c</b>) SEM electron microscope photo at 200 times; (<b>d</b>) SEM electron microscope photo at 1000 times.</p>
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<p>SEM electron micrograph of fatigue final fracture region. (<b>a</b>) SEM electron microscope photo at 50 times; (<b>b</b>) SEM electron microscope photo at 100 times; (<b>c</b>) SEM electron microscope photo at 500 times; (<b>d</b>) SEM electron microscope photo at 1000 times.</p>
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<p>Stereo microscopic results of the fracture.</p>
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<p>Fatigue stripes at different crack lengths in the crack growth region.</p>
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<p>Relationship between crack growth rate da/dN and crack length <span class="html-italic">a</span>.</p>
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20 pages, 8161 KiB  
Article
Research on Support Technology for Unstable Roof Roadway Under Abandoned Roadways in Ultra-Thick Coal Seam
by Xianyang Yu, Siyuan Lv, Yafei Luo, Pengchao Liu, Hao Fu and Yicai Zhou
Processes 2024, 12(12), 2886; https://doi.org/10.3390/pr12122886 - 17 Dec 2024
Viewed by 515
Abstract
Due to the impact of disordered mining activities in previous years, numerous abandoned roadways exist in the second mining district of the 13# coal seam in Chejiazhuang Coal Mine. The stability of the new roadway roof was analyzed under various distributions of abandoned [...] Read more.
Due to the impact of disordered mining activities in previous years, numerous abandoned roadways exist in the second mining district of the 13# coal seam in Chejiazhuang Coal Mine. The stability of the new roadway roof was analyzed under various distributions of abandoned roadways above. It was determined that the ultimate stable thickness of the coal layer between the new and abandoned roadways is 4.0 m. When the thickness between the two is less than 4.0 m, the roof becomes unstable after excavation, posing a risk of collapse. Advanced grouting reinforcement is required to enhance roof stability before installing U-shaped steel arches. Mechanical experiments were conducted on the polymer grouting consolidation of fractured coal, showing a significant increase in residual strength compared to intact coal. Furthermore, the uniaxial compressive strength of the polymer grouting consolidation partially recovered. On average, the consolidation coefficient and recovery coefficient were 5.28 and 85.51%, respectively. Grouting increased the ductility of the fractured surrounding rock, enhancing its resistance to deformation and plasticity. A polymer grouting consolidation technology for supporting fractured surrounding rock under the unstable roof of abandoned roadways is proposed, along with the design of corresponding support schemes and parameters. Monitoring the results of mine pressure indicated that the surrounding rock remained stable after roadway excavation, validating the effectiveness of the support schemes and parameters. Full article
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<p>The engineering site in the Shanxi Provence of China.</p>
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<p>Roadway in Chejiazhuang Coal Mine with unstable roof.</p>
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<p>Stratigraphic column of 13# coal seam in Chejiazhuang Coal Mine.</p>
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<p>Mechanical model of roof rock beam of new roadway under abandoned roadway.</p>
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<p>Relationship between roof thickness and tensile stress in the midpoint of the lower layer of the rock beam.</p>
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<p>The cohesion of coal and fractured coal grouting consolidation.</p>
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<p>Calibrating the strain softening model for coal and fractured coal grouting consolidation (the test process of the mechanical parameters of coal and fractured coal grouting consolidation is introduced in <a href="#sec4-processes-12-02886" class="html-sec">Section 4</a>).</p>
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<p>Numerical simulation model and meshing.</p>
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<p>Plastic zone and fractured zone around abandoned roadway.</p>
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<p>Plastic zone and fracture zone of surrounding rock with roof thickness of 3.0 m.</p>
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<p>Plastic zone and fractured zone of surrounding rock with roof thickness of 3.5 m.</p>
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<p>Plastic zone and fractured zone of surrounding rock with roof thickness of 4.0 m.</p>
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<p>Plastic zone and fractured zone of surrounding rock with roof thickness of 4.5 m.</p>
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<p>Fracture coal grouting test’s flow chat.</p>
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<p>Grouting consolidation test equipment.</p>
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<p>Fractured coal grouting consolidation. (<b>a</b>) Fractured coal grouting consolidation; (<b>b</b>) fractured grouting consolidation.</p>
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<p>Interact coal and fractured coal grouting consolidation strength curve.</p>
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<p>Development of plastic zone and fractured zone in surrounding rock with polymer grouting (unstable roof).</p>
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<p>Support parameters for the roadway with an unstable roof under abandoned roadways (dimensions in the figure are given in millimeters (mm)). (<b>a</b>) A longitudinal section of the roadway (<b>b</b>) A cross-section of the roadway.</p>
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<p>Roadway’s surrounding rock displacement in monitoring site. (The red circle indicates the short anchor bolts installed in the surrounding rock. An L-shaped thick wire is welded to the nut of the bolt, which is used to observe the displacement of the surrounding rock in the roadway).</p>
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<p>Monitoring results of surface displacement in new roadway.</p>
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<p>The overall condition of the roadway after being supported.</p>
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19 pages, 7133 KiB  
Article
Fatigue Crack Growth Monitoring and Investigation on G20Mn5QT Cast Steel and Welds via Acoustic Emission
by Qingyang Liu, Zhenli Zhang, Giuseppe Lacidogna, Yantao Xu and Jie Xu
Appl. Sci. 2024, 14(20), 9612; https://doi.org/10.3390/app14209612 - 21 Oct 2024
Viewed by 1093
Abstract
The fatigue crack growth properties of G20Mn5QT cast steel and corresponding butt welds, using compact tension specimens, were monitored and investigated via acoustic emission (AE) techniques. Fatigue crack growth is a combination of cyclic plastic deformations before the crack tip, tensile crack fractures, [...] Read more.
The fatigue crack growth properties of G20Mn5QT cast steel and corresponding butt welds, using compact tension specimens, were monitored and investigated via acoustic emission (AE) techniques. Fatigue crack growth is a combination of cyclic plastic deformations before the crack tip, tensile crack fractures, and shear crack fractures. The cyclic plastic deformations release the maximum amount of energy, which accounts for half of the total energy, and the second-largest number of AE signals, which are of the continuous-wave type. The tensile crack fractures release the second-largest amount of energy and the largest number of AE signals, which are of the burst-wave type. The shear crack fractures release the least amount of energy and the lowest number of AE signals, which are similar to the burst type, albeit with a relatively longer rise time and duration. Crack tip advancement can be regarded as a discontinuous process. The critical area before the crack tip brittlely ruptures when the fatigue damage caused by cyclic plastic deformations reaches critical status. The ruptures produce a large number of tensile crack fractures and rare shear crack fractures. Through fractography observation, the shear crack fractures occur probabilistically around defects caused by casting or welding, which lead to stress and strain in the local complex. Full article
(This article belongs to the Collection Nondestructive Testing (NDT))
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<p>Microstructures: (<b>a</b>) G20Mn5QT cast steel; (<b>b</b>) welds.</p>
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<p>Specimen machining zone.</p>
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<p>Geometry of CT specimen.</p>
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<p>Test setup.</p>
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<p>Fatigue crack length vs. load cycles.</p>
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<p>Fatigue crack growth rate vs. stress intensity factor range.</p>
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<p>AE hit and energy release rates.</p>
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<p>AE normalized cumulative hit and energy.</p>
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<p>Cluster analysis of G20Mn5QT and weld: (<b>a</b>) DB index; (<b>b</b>) proportion of each cluster.</p>
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<p>Waveforms of typical AE signals in different clusters: (<b>a</b>) cluster 1 signals of G20Mn5QT; (<b>b</b>) cluster 1 signals of welds; (<b>c</b>) cluster 2 signals of G20Mn5QT; (<b>d</b>) cluster 2 signals of welds; (<b>e</b>) cluster 3 signals of G20Mn5QT; (<b>f</b>) cluster 3 signals of welds.</p>
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<p>Correlation plot between RA and AF.</p>
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<p>Frequency spectra of typical AE signals in different clusters: (<b>a</b>) cluster 1 signals of G20Mn5QT; (<b>b</b>) cluster 1 signals of welds; (<b>c</b>) cluster 2 signals of G20Mn5QT; (<b>d</b>) cluster 2 signals of welds; (<b>e</b>) cluster 3 signals of G20Mn5QT; (<b>f</b>) cluster 3 signals of welds.</p>
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<p>Wave characteristics for each cluster: (<b>a</b>) G20Mn5QT; (<b>b</b>) weld.</p>
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<p>Cumulative AE of different clusters for G20Mn5QT: (<b>a</b>) hit; (<b>b</b>) energy.</p>
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<p>Cumulative AE of different clusters for the weld: (<b>a</b>) hit; (<b>b</b>) energy.</p>
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<p>Scanning electron micrographs of crack surfaces: (<b>a</b>,<b>c</b>,<b>e</b>,<b>g</b>) G20Mn5QT cast steel; (<b>b</b>,<b>d</b>,<b>f</b>,<b>h</b>) butt weld; (<b>a</b>,<b>b</b>) crack surface; (<b>c</b>,<b>d</b>) fatigue striations at stage I; (<b>e</b>,<b>f</b>) fatigue striations at stage II; (<b>g</b>,<b>h</b>) dimples at stage III.</p>
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<p>Scanning electron micrographs of crack surfaces: (<b>a</b>) shear bands of G20Mn5QT cast steel; (<b>b</b>) shear bands of butt weld.</p>
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11 pages, 6610 KiB  
Article
Molecular Dynamics Study of Bending Deformation of Mo2Ti2C3 and Ti4C3 (MXenes) Nanoribbons
by Vadym Borysiuk, Iakov A. Lyashenko and Valentin L. Popov
Molecules 2024, 29(19), 4668; https://doi.org/10.3390/molecules29194668 - 1 Oct 2024
Viewed by 988
Abstract
We report a computational study of the bending deformation of two-dimensional nanoribbons by classical molecular dynamics methods. Two-dimensional double transition metal carbides, together with monometallic ones, belong to the family of novel nanomaterials, so-called MXenes. Recently, it was reported that within molecular dynamics [...] Read more.
We report a computational study of the bending deformation of two-dimensional nanoribbons by classical molecular dynamics methods. Two-dimensional double transition metal carbides, together with monometallic ones, belong to the family of novel nanomaterials, so-called MXenes. Recently, it was reported that within molecular dynamics simulations, Ti4C3 MXene nanoribbons demonstrated higher resistance to bending deformation than thinner Ti2C MXene and other two-dimensional materials, such as graphene and molybdenum disulfide. Here, we apply a similar method to that used in a previous study to investigate the behavior of Mo2Ti2C3 nanoribbon under bending deformation, in comparison to the Ti4C3 sample that has a similar structure. Our calculations show that Mo2Ti2C3 is characterized by higher bending rigidity at DTi2Mo2C392.15 eV than monometallic Ti4C3 nanoribbon at DTi4C372.01 eV, which has a similar thickness. Moreover, approximately the same magnitude of critical central deflection of the nanoribbon before fracture was observed for both Mo2Ti2C3 and Ti4C3 samples, wc1.7 nm, while Mo2Ti2C3 MXene is characterized by almost two times higher critical value of related external force. Full article
(This article belongs to the Special Issue The Way Forward in MXenes Materials)
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<p>Atomistic configurations of the studied Mo<sub>2</sub>Ti<sub>2</sub>C<sub>3</sub> (<b>left panel</b>) and Ti<sub>4</sub>C<sub>3</sub> (<b>right panel</b>) samples. Related colors of the atoms are shown in the figure.</p>
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<p>Snapshots (top view in Cartesian coordinate system XYZ) of the initial configuration of the studied Ti<sub>4</sub>C<sub>3</sub> (<b>top panel</b>) and Mo<sub>2</sub>Ti<sub>2</sub>C<sub>3</sub> (<b>bottom panel</b>) nanoribbons. The colors of atoms are the same as in <a href="#molecules-29-04668-f001" class="html-fig">Figure 1</a>.</p>
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<p>Schematics of the experiments on the bending of Mo<sub>2</sub>Ti<sub>2</sub>C<sub>3</sub> and Ti<sub>4</sub>C<sub>3</sub> nanoribbons in Cartesian coordinate system XYZ. Fixed atoms, on the edges of the sample and central atoms to which external bending load is applied, are shown in red color. Constrained atoms across long edges are denoted in green.</p>
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<p>Time dependencies of the <span class="html-italic">Z</span> coordinate of centers of the samples. Panel (<b>a</b>) shows the behavior of the samples in the initial stage of the experiment for the first three steps of loading, while panel (<b>b</b>) demonstrates the behavior in the middle of simulations.</p>
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<p>(<b>a</b>) Time dependencies of <span class="html-italic">Z</span> coordinate of Ti<sub>4</sub>C<sub>3</sub> nanoribbon during bending with different force increments, <math display="inline"><semantics> <mrow> <mo>Δ</mo> <mi>F</mi> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <mn>2</mn> <mo>Δ</mo> <mi>F</mi> </mrow> </semantics></math> (magnitudes of central deflection and force increments are shown in the figure). Time dependencies of <span class="html-italic">Z</span> coordinate of Mo<sub>2</sub>Ti<sub>2</sub>C<sub>3</sub> nanoribbons during indentation and relaxation (<b>b</b>).</p>
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<p>(<b>a</b>) Time dependencies of <span class="html-italic">Z</span> coordinate of Ti<sub>4</sub>C<sub>3</sub> and Mo<sub>2</sub>Ti<sub>2</sub>C<sub>3</sub> nanoribbons during the whole experiment. (<b>b</b>) Corresponding load curves <math display="inline"><semantics> <mrow> <mi>w</mi> <mrow> <mo>(</mo> <mi>F</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> for Ti<sub>4</sub>C<sub>3</sub> and Mo<sub>2</sub>Ti<sub>2</sub>C<sub>3</sub> nanoribbons. The final points on the dependencies plotted in panel (<b>b</b>) do not relate to corresponding magnitude of central deflection of nanoribbons; these points were measured after the fracture of nanoribbons in the certain time moments, according to computational algorithm and plotted in the figure to illustrate the fracturing of the samples.</p>
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<p>Examples of typical atomistic configuration of Mo<sub>2</sub>Ti<sub>2</sub>C<sub>3</sub> (<b>left panel</b>) and Ti<sub>4</sub>C<sub>3</sub> (<b>right panel</b>) nanoribbons at different magnitudes of central deflection. The bottom panels show the plastic deformation of the Mo<sub>2</sub>Ti<sub>2</sub>C<sub>3</sub> sample and the fracture of the Ti<sub>4</sub>C<sub>3</sub> nanoribbon.</p>
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<p>The dependence of bending rigidity <span class="html-italic">D</span> of Mo<sub>2</sub>Ti<sub>2</sub>C<sub>3</sub> and Ti<sub>4</sub>C<sub>3</sub> samples, calculated from the data shown in <a href="#molecules-29-04668-f006" class="html-fig">Figure 6</a>b, according to Equation (1).</p>
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<p>The dependence of bending rigidity <span class="html-italic">D</span> of Mo<sub>2</sub>Ti<sub>2</sub>C<sub>3</sub> and Ti<sub>4</sub>C<sub>3</sub> samples, calculated from the data shown in <a href="#molecules-29-04668-f006" class="html-fig">Figure 6</a>b, according to Equation (1), taking into account of the pre-tension of the sample. Inset shows related dependencies of effective spring constant <math display="inline"><semantics> <mrow> <msub> <mi>k</mi> <mrow> <mi>e</mi> <mi>f</mi> <mi>f</mi> </mrow> </msub> <mo>=</mo> <mi>F</mi> <mo>/</mo> <mi>w</mi> </mrow> </semantics></math>.</p>
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15 pages, 4972 KiB  
Article
Energy Evolution Characteristics and Hydraulic Fracturing Roof Cutting Technology for Hard Roof Working Face during Initial Mining: A Case Study
by Chungang Wang, Jianbiao Bai, Tianchen Wang and Wenda Wu
Appl. Sci. 2024, 14(16), 7405; https://doi.org/10.3390/app14167405 - 22 Aug 2024
Viewed by 910
Abstract
In the process of mining, a large area of hard roof will be exposed above a goaf and may suddenly break. This can easily induce rock burst and has a significant impact on production safety. In this study, based on the engineering background [...] Read more.
In the process of mining, a large area of hard roof will be exposed above a goaf and may suddenly break. This can easily induce rock burst and has a significant impact on production safety. In this study, based on the engineering background of the hard roof of the 2102 working face in the Balasu coal mine, the spatial and temporal characteristics of the strain energy of the roof during the initial mining process were explored in depth. Based on a theoretical calculation, it is proposed that hydraulic fracturing should be carried out in the medium-grained sandstone layer that is 4.8–22.43 m above the roof, and that the effective fracturing section in the horizontal direction should be within 30.8 m of the cutting hole of the working face. The elastic strain energy fish model was established in FLAC3D to analyze the strain energy accumulation of the roof during the initial mining process. The simulation and elastic strain energy results show that, as the working face advances to 70–80 m, the hard roof undergoes significant bending deformation. The energy gradient increases with the rapid accumulation of strain energy to a peak value of 140.54 kJ/m3. If the first weighting occurs at this moment in time, the sudden fracture of the roof will be accompanied by the release of elastic energy, which will induce rock burst. Therefore, it is necessary to implement roof cutting and pressure relief before reaching the critical step of 77 m. To this end, the comprehensive hydraulic fracturing technology of ‘conventional short drilling + directional long drilling’ is proposed. A field test shows that the hydraulic fracturing technology effectively weakens the integrity of the rock layer. The first weighting interval is 55 m, and it continues until the end of the pressure at the 70 m position. The roof collapses well, and the mining safety is improved. This study provides an important reference for hard roof control. Full article
(This article belongs to the Special Issue Underground Rock Support and Excavation)
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<p>Layout of longwall panel 2102. (<b>a</b>) Panel layout. (<b>b</b>) Generalized stratigraphy column.</p>
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<p>Asymmetric three-hinged arch structure of initial roof caving.</p>
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<p>Model overview.</p>
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<p>Temporal and spatial distribution characteristics of elastic strain energy density during mining to (<b>a</b>) 10, (<b>b</b>) 20, (<b>c</b>) 30, (<b>d</b>) 40, (<b>e</b>) 50, (<b>f</b>) 60, (<b>g</b>) 70, and (<b>h</b>) 80 m.</p>
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<p>Temporal and spatial distribution characteristics of elastic strain energy density during mining to (<b>a</b>) 10, (<b>b</b>) 20, (<b>c</b>) 30, (<b>d</b>) 40, (<b>e</b>) 50, (<b>f</b>) 60, (<b>g</b>) 70, and (<b>h</b>) 80 m.</p>
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<p>Principle of conventional straight-hole hydraulic fracturing technology. (<b>a</b>) The first section of construction. (<b>b</b>) Section n of construction.</p>
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<p>Principle of directional-hole hydraulic fracturing technology. (<b>a</b>) The first section of construction. (<b>b</b>) Section n of construction.</p>
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<p>Hydraulic fracturing roof cutting scheme. (<b>a</b>) Hydraulic fracturing drilling plane diagram. Drilling profile of hydraulic fracturing holes (<b>b</b>) S, L, B, and D, and (<b>c</b>) A, C, and D.</p>
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<p>Curve of hydraulic fracturing water pressure and flow rate vs. time. Boreholes (<b>a</b>) A3 and (<b>b</b>) L12.</p>
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<p>Drilling peep to detect crack propagation after hydraulic fracturing.</p>
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<p>The working resistance of the support during the mining of the 2102 working face.</p>
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<p>The roof collapse behind the support of the 2102 working face.</p>
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23 pages, 1388 KiB  
Article
Continuum–Discontinuum Bonded-Block Model for Simulating Mixed-Mode Fractures
by Yue Sun, Tao Chen, Longquan Yong and Qian Chen
Mathematics 2024, 12(16), 2533; https://doi.org/10.3390/math12162533 - 16 Aug 2024
Viewed by 964
Abstract
In this study, an improved discontinuous deformation analysis method with sub-block strategy is introduced to numerically simulate mixed-mode fractures. This approach partitions the material domain into continuum and potential discontinuum regions, applying specialized modeling techniques to each. In the continuum region, penalty-like bonding [...] Read more.
In this study, an improved discontinuous deformation analysis method with sub-block strategy is introduced to numerically simulate mixed-mode fractures. This approach partitions the material domain into continuum and potential discontinuum regions, applying specialized modeling techniques to each. In the continuum region, penalty-like bonding springs are employed to glue the sub-blocks together to capture the elastic behavior of the material. In the potential discontinuum region, the cohesive springs with the stiffness based on the cohesive zone model are implemented between sub-blocks to reproduce the process of crack nucleation and propagation. The primary advantage of this method is its capability to effectively model the transition of quasi-brittle solids from a continuous to a discontinuous stage through the degradation of cohesive springs. This accurately represents material failure while maintaining stability and consistency along uncracked interfaces. Another significant benefit is the method’s efficiency, as it avoids complex contact operations along sub-block interfaces before the cohesive spring between them fails. Validation through various benchmark numerical examples, such as cantilever beam-bending and diverse fracture simulations, demonstrates the method’s accuracy and robustness by comparing the results with analytical solutions. These comparisons show that the proposed method effectively captures the interplay between tensile and shear traction components in the mixed-mode crack propagation process. Full article
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<p>Discretization diagram of CDBBM for continuum subdomain and potential discontinuum subdomain.</p>
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<p>Schematic diagram of BSs that glue adjacent sub-blocks within the C-domain.</p>
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<p>Schematic diagram of CSs that connect adjacent sub-blocks within the D-domain.</p>
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<p>The bi-linear TSL relations for CS stiffness.</p>
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<p>Mixed-mode failure criteria for CSs.</p>
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<p>Flowchart of all computational modules of the CDBBM.</p>
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<p>Geometry of the cantilever.</p>
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<p>Different uniform meshes for subdividing the cantilever beam as shown in <a href="#mathematics-12-02533-f007" class="html-fig">Figure 7</a>.</p>
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<p>Comparing the result computed by the CDBBM using different spatial discretization strategies with the analytical solution and the result by the original DDA.</p>
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<p>Geometry configuration for the specimen used in the DCB test.</p>
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<p>The subdivision adopted by the CDBBM for the DCB test.</p>
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<p>The results computed by the CDBBM with the loading rate <math display="inline"><semantics> <mrow> <mi>v</mi> <mo>=</mo> <mn>0.001</mn> </mrow> </semantics></math> mm/ms at <math display="inline"><semantics> <mrow> <mi>t</mi> <mo>=</mo> <mn>1200</mn> </mrow> </semantics></math> ms for the DCB test.</p>
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<p>Results compared to analytical solutions with different loading rates <span class="html-italic">v</span>.</p>
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<p>Results compared to analytical solutions with different critical stresses <math display="inline"><semantics> <msub> <mi>σ</mi> <mi>c</mi> </msub> </semantics></math>.</p>
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<p>Results compared to analytical solutions with different fracture toughnesses <math display="inline"><semantics> <msub> <mi>G</mi> <mi>Ic</mi> </msub> </semantics></math>.</p>
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<p>The geometry configuration for the ENF test: the length <math display="inline"><semantics> <mrow> <mn>2</mn> <mi>L</mi> <mo>=</mo> <mn>30.3</mn> </mrow> </semantics></math> mm, the half-height <math display="inline"><semantics> <mrow> <mi>h</mi> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math> mm, the out-of-plane thickness <math display="inline"><semantics> <mrow> <mi>B</mi> <mo>=</mo> <mn>3</mn> </mrow> </semantics></math> mm, and the length of pre-existing crack <math display="inline"><semantics> <mrow> <msub> <mi>a</mi> <mn>0</mn> </msub> <mo>=</mo> <mn>9</mn> </mrow> </semantics></math> mm.</p>
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<p>The uniform quadrilateral sub-block mesh for the ENF test.</p>
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<p>The results computed by the CDBBM for the ENF test with <math display="inline"><semantics> <mrow> <msub> <mi>τ</mi> <mi>c</mi> </msub> <mo>=</mo> <mn>220</mn> </mrow> </semantics></math> MPa at <math display="inline"><semantics> <mrow> <mi>t</mi> <mo>=</mo> <mn>1800</mn> </mrow> </semantics></math> ms.</p>
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<p>Results compared with analytical solution for the ENF test using different critical stresses.</p>
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<p>Geometry configuration of the MMB test. The specimen has a length of <math display="inline"><semantics> <mrow> <mn>2</mn> <mi>L</mi> <mo>=</mo> <mn>30</mn> </mrow> </semantics></math> mm, the half-height <math display="inline"><semantics> <mrow> <mi>h</mi> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math> mm, the out-of-plane thickness <math display="inline"><semantics> <mrow> <mi>B</mi> <mo>=</mo> <mn>5</mn> </mrow> </semantics></math> mm, and the pre-existing crack length <math display="inline"><semantics> <mrow> <msub> <mi>a</mi> <mn>0</mn> </msub> <mo>=</mo> <mn>9</mn> </mrow> </semantics></math> mm. The long lever above the specimen has the size parameters <math display="inline"><semantics> <mrow> <mi>c</mi> <mo>=</mo> <mn>13.1</mn> </mrow> </semantics></math> mm.</p>
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<p>The uniform quadrilateral sub-block mesh for the MMB test. A total of 3310 quadrilateral sub-blocks are employed.</p>
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<p>The deformation and stress distribution computed by the improved SDDA approach in the MMB test with the loading rate <math display="inline"><semantics> <mrow> <mi>v</mi> <mo>=</mo> <mn>0.001</mn> </mrow> </semantics></math> mm/ms at <math display="inline"><semantics> <mrow> <mi>t</mi> <mo>=</mo> <mn>2500</mn> </mrow> </semantics></math> ms.</p>
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<p>CDBBM simulation results against the analytical solution for the MMB test with varying normal cohesive strengths <math display="inline"><semantics> <mrow> <msub> <mi>σ</mi> <mi>c</mi> </msub> <mo>=</mo> <mn>4</mn> <mo>,</mo> <mn>7</mn> <mo>,</mo> </mrow> </semantics></math> and 10 MPa and the shear cohesive strength <math display="inline"><semantics> <mrow> <msub> <mi>τ</mi> <mi>c</mi> </msub> <mo>=</mo> <mn>7</mn> </mrow> </semantics></math> MPa.</p>
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<p>CDBBM simulation results against the analytical solution for the MMB test with the normal cohesive strength <math display="inline"><semantics> <mrow> <msub> <mi>σ</mi> <mi>c</mi> </msub> <mo>=</mo> <mn>7</mn> </mrow> </semantics></math> MPa and the varying shear cohesive strengths <math display="inline"><semantics> <mrow> <msub> <mi>τ</mi> <mi>c</mi> </msub> <mo>=</mo> <mn>4</mn> <mo>,</mo> <mn>7</mn> <mo>,</mo> </mrow> </semantics></math> and 10 MPa.</p>
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14 pages, 6157 KiB  
Article
Experimental Investigations into Failures and Nonlinear Behaviors of Structural Membranes with Open Cuttings
by Wenrui Li, Ping Liu, Baijian Tang and Sakdirat Kaewunruen
Appl. Sci. 2024, 14(14), 6241; https://doi.org/10.3390/app14146241 - 18 Jul 2024
Viewed by 1009
Abstract
Reportedly, structural failures in membrane structures have occurred frequently, mostly originating from localized damage caused by intense loads on the membrane surface. It is thus necessary to investigate the nonlinear behaviors and load-carrying capacity of membranes with local damage. This study has conducted [...] Read more.
Reportedly, structural failures in membrane structures have occurred frequently, mostly originating from localized damage caused by intense loads on the membrane surface. It is thus necessary to investigate the nonlinear behaviors and load-carrying capacity of membranes with local damage. This study has conducted uniaxial tensile tests for membranes with a variety of original defects by using a specialized experimental setup and photogrammetry technique. The nonlinear relationship between the mechanical properties and the deforming angle of membranes, which portrays the principal axis, tensor, tensile stress, and position of the original defects, is investigated. The entire process of membrane failure has been recorded, and the strain and stress during each test specimen are compared. The new results indicate that the membranes exhibit predominantly elastic deformation before failure but surprisingly impart brittle fracture upon failure. Finally, a novel approach for estimating the load-bearing capacity of initially damaged membranes was proposed through the analysis of the load-bearing capacity of the damaged membranes under various conditions, positions, angles, and other influential factors. Full article
(This article belongs to the Special Issue The Applications of Nonlinear Dynamics in Materials and Structures)
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<p>The typical tensile membrane structure.</p>
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<p>Schematic diagram of membrane specimens.</p>
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<p>Schematic diagram of calibration points.</p>
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<p>Schematic diagram of self-made test device. (<b>a</b>) Initial crack location of the specimen. (<b>b</b>) Device dimension diagram.</p>
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<p>Schematic diagram of membrane material damage under various cases.</p>
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<p>Calibration point distances for each stage of Case 3.</p>
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<p>Calibration point distances for each stage of Case 3.</p>
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<p>Stress–strain curve under working Case 1–5.</p>
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<p>Stress–strain curve under working Cases 6–10.</p>
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<p>Angles and ultimate strength curves in two type cases.</p>
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<p>Test slit extension example.</p>
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<p>The mechanic of the membrane from crack to failure.</p>
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<p>Fitted curve and the test data.</p>
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19 pages, 6384 KiB  
Article
Influence of Mechanical Loading on the Process of Tribochemical Action on Physicochemical and Biopharmaceutical Properties of Substances, Using Lacosamide as an Example: From Micronisation to Mechanical Activation
by Elena V. Uspenskaya, Ekaterina Kuzmina, Hoang Thi Ngoc Quynh, Maria A. Komkova, Ilaha V. Kazimova and Aleksey A. Timofeev
Pharmaceutics 2024, 16(6), 798; https://doi.org/10.3390/pharmaceutics16060798 - 13 Jun 2024
Cited by 1 | Viewed by 1113
Abstract
Many physical and chemical properties of solids, such as strength, plasticity, dispersibility, solubility and dissolution are determined by defects in the crystal structure. The aim of this work is to study in situ dynamic, dispersion, chemical, biological and surface properties of lacosamide powder [...] Read more.
Many physical and chemical properties of solids, such as strength, plasticity, dispersibility, solubility and dissolution are determined by defects in the crystal structure. The aim of this work is to study in situ dynamic, dispersion, chemical, biological and surface properties of lacosamide powder after a complete cycle of mechanical loading by laser scattering, electron microscopy, FR-IR and biopharmaceutical approaches. The SLS method demonstrated the spontaneous tendency toward surface-energy reduction due to aggregation during micronisation. DLS analysis showed conformational changes of colloidal particles as supramolecular complexes depending on the loading time on the solid. SEM analysis demonstrated the conglomeration of needle-like lacosamide particles after 60 min of milling time and the transition to a glassy state with isotropy of properties by the end of the tribochemistry cycle. The following dynamic properties of lacosamide were established: elastic and plastic deformation boundaries, region of inhomogeneous deformation and fracture point. The ratio of dissolution-rate constants in water of samples before and after a full cycle of loading was 2.4. The lacosamide sample, which underwent a full cycle of mechanical loading, showed improved kinetics of API release via analysis of dissolution profiles in 0.1 M HCl medium. The observed activation-energy values of the cell-death biosensor process in aqueous solutions of the lacosamide samples before and after the complete tribochemical cycle were 207 kJmol−1 and 145 kJmol−1, respectively. The equilibrium time of dissolution and activation of cell-biosensor death corresponding to 20 min of mechanical loading on a solid was determined. The current study may have important practical significance for the transformation and management of the properties of drug substances in solid form and in solutions and for increasing the strength of drug matrices by pre-strain hardening via structural rearrangements during mechanical loading. Full article
(This article belongs to the Special Issue Novel Dry Powder Formulation and Delivery Systems)
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<p>Stages and advantages of mechanochemistry.</p>
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<p>Crystal defects: (<b>a</b>) point defects (zero-dimensional); (<b>b</b>) line defects (1D); (<b>c</b>) surface defects (2D); (<b>d</b>) volume defects (3D).</p>
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<p>Chemical structure of lacosamide [<a href="#B31-pharmaceutics-16-00798" class="html-bibr">31</a>].</p>
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<p>Principal schematic of the equipment for carrying out tribochemical processes.</p>
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<p>Kinetic scheme of ligand-receptor interaction <span class="html-italic">Sp. ambigua</span> with toxicant: C-cell, L-ligand, <span class="html-italic">n</span>-stoichiometric coefficient, C·L<sub>n</sub>—intermediate state (cell after interaction with the ligand), K<sub>e</sub> is the equilibrium constant fast stage, f<sub>m</sub> is the rate constant of the cell transition to the dead state, DC is a dead cell. The inserts show photographs of ciliates at the stages of incubation in the medium and recording of death.</p>
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<p>Dispersive properties of lacosamide samples at different times of Trb impact according to the SLS method: (<b>a</b>) Particle size distributions; (<b>b</b>) Integral dispersion characteristics—laser obscuration, volume concentration, V(%); specific surface area, ssa (m<sup>2</sup>/cm<sup>3</sup>). Insets show the morphology of Lcs crystals before and after high-intensity ML.</p>
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<p>Dispersive properties of lacosamide samples under different Trb impact times according to the DLS method: (<b>a</b>) particle-size distributions in units of laser light-scattering intensity; (<b>b</b>) 2D data diagram of the average count rate and nanodispersion size; (<b>c</b>) ξ-potential (mV) and polydispersity index value (PDI).</p>
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<p>FT-IR spectra of Lcs samples before and after Trb impact: (<b>a</b>) Full range (the inset shows a naive Lcs sample); (<b>b</b>) Spectra of loaded samples “subtraction” from native Lcs (the inset shows the amplitude vibrations of the transmission maximum at 3280 cm<sup>−1</sup>, corresponding to the NH group); (<b>c</b>) Dependence of the signal-to-noise value on the wave number (cm<sup>−1</sup>); (<b>d</b>) High-frequency region (3200–2700 cm<sup>−1</sup>) of the range of characteristic vibrations of bonds (the insets shows the spectrum regions with reflected transmission for Lcs samples at t<sub>ML</sub> = 80 min and t<sub>ML</sub> = 90 min).</p>
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<p>SEM micrographs for Lcs obtained at different times of high-intensity ML and: (<b>a</b>) t = 0 min; (<b>b</b>) t = 60 min; (<b>c</b>) t = 90 min. Device magnification (MAG) = 9.81–3.00 kx. The insets show the particle size distribution according to the DLS method.</p>
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<p>The Lsc’ samples dissolution in water as measured by LALLS method: In direct (<b>a</b>) and semi-logarithmic (<b>b</b>) coordinates.</p>
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<p>Stress–strain curve. (<b>a</b>) Temperature curve of the heating inside the milling bowl-duration of the applied ML (<b>b</b>) Typical of SB stress–strain curve.</p>
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<p>2D-diagrams showing the dependence of the parameters of dissolution in water and death of the <span class="html-italic">Spirostomum ambigua A</span> cell biosensor in 0.5% aqueous solutions of various ML Lcs samples: (<b>a</b>) Time and dissolution-rate constant; (<b>b</b>) activation energy of cell transformations.</p>
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<p>Cumulative dissolution profiles of lacosamide samples unloaded (black) and loaded (red) in simulated gastric fluid obtained using the USP II apparatus. The results are expressed as mean ± RSD (<span class="html-italic">n</span> = 6).</p>
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17 pages, 5225 KiB  
Article
Laboratory Study of Liquid Nitrogen Cryo-Fracturing as an Environmentally Friendly Approach for Coalbed Methane (CBM) Reservoirs
by Sotirios Nik. Longinos, Alina Serik, Emil Bayramov, Medet Junussov, Dastan Begaliyev and Randy Hazlett
Energies 2024, 17(10), 2359; https://doi.org/10.3390/en17102359 - 14 May 2024
Cited by 3 | Viewed by 1160
Abstract
This study evaluated two distinct cryo-fracturing techniques using liquid nitrogen (LN2). The evaluation included tests for peak compression strength, acoustic emission, and energy absorption. The experiments compared single-exposure freezing time (FT) and multiple-exposure freezing–thawing cycle (FTC) processes on dried specimens. The [...] Read more.
This study evaluated two distinct cryo-fracturing techniques using liquid nitrogen (LN2). The evaluation included tests for peak compression strength, acoustic emission, and energy absorption. The experiments compared single-exposure freezing time (FT) and multiple-exposure freezing–thawing cycle (FTC) processes on dried specimens. The outcomes indicated that FTC experiments demonstrated lower uniaxial compression stress (UCS) values compared to FT experiments because, during the thawing phase, the ice inside the pores reverts to liquid as the temperature rises. The difference between average baseline experiments versus FT180 and FTC6 indicated a reduction in stress of 14.5% and 38.5%, respectively. The standard error of our experiments ranged from 0.58% for FT60 to 5.35% for FTC6. The damage factor follows a downward trend in both FT and FTC experiments as the time of LN2 treatment augments. The amount of energy that can be absorbed in elastic or plastic deformation before failure is less for FTC specimens with the same total LN2 exposure time. Samples undergoing the freezing time process demonstrate a greater and denser quantity of acoustic emissions in comparison to freezing–thawing cycle processes, suggesting a positive correlation with uniaxial compressive strength outcomes. The large network of fractures formed by the FTC and PFTC techniques indicated that they have the greatest potential as stimulation approaches. The engineering results were improved by adding the geological context, which is essential to apply these findings to coals that have comparable origins. Full article
(This article belongs to the Section H: Geo-Energy)
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<p>Synthetic coal preparation of cube specimens.</p>
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<p>Physical processes in the experimental protocol before examination of our coal specimens.</p>
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<p>Uniaxial stress vs. time curves. The first try (<b>a</b>), second try (<b>b</b>), third try (<b>c</b>) and fourth try (<b>d</b>) of experiments.</p>
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<p>Compression strength vs. FT (<b>a</b>) and FTC (<b>b</b>) processes.</p>
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<p>Damage factor vs. process for both FT (<b>a</b>) and FTC (<b>b</b>) methods.</p>
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<p>Load vs. displacement curves.</p>
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<p>Absorbed energy vs. process curves for FT (<b>a</b>) and FTC (<b>b</b>) methods.</p>
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<p>Specimen before compression test (<b>left</b>) and specimen after compression test (<b>right</b>).</p>
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<p>Compressive strength and acoustic emissions for different LN<sub>2</sub> treatments: (<b>a</b>) Baseline; (<b>b</b>) FT60 Specimen-1; (<b>c</b>) FT120 Specimen-1; and (<b>d</b>) FT180 Specimen-1.</p>
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<p>Compressive strength and acoustic emissions for different LN<sub>2</sub> treatments: (<b>a</b>) Baseline; (<b>b</b>) FTC2 Specimen-1; (<b>c</b>) FTC4 Specimen-1; and (<b>d</b>) FTC6 Specimen-1.</p>
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