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18 pages, 5276 KiB  
Article
The Pore Structure Characteristics of Mortar and Its Application in the Study of Chloride Ion Transport Performance
by Zhidan Rong, Hanliang Ouyang, Yun Gao and Hao Chen
Buildings 2025, 15(3), 383; https://doi.org/10.3390/buildings15030383 - 26 Jan 2025
Viewed by 415
Abstract
The cement-based materials widely used in infrastructure construction, such as bridges and ports, are subjected to seawater erosion and medium erosion during their service life, and their durability has always been a concern. The diffusion coefficient of chloride ions is an important indicator [...] Read more.
The cement-based materials widely used in infrastructure construction, such as bridges and ports, are subjected to seawater erosion and medium erosion during their service life, and their durability has always been a concern. The diffusion coefficient of chloride ions is an important indicator in the research of cement-based materials’ durability, and the pore structure is one of the most fundamental reasons affecting the diffusion behavior of chloride ions. In this paper, Mercury intrusion porosimetry (MIP), Nuclear magnetic resonance (NMR), and Nitrogen adsorption method (NAD) were used to analyze the pore structures of mortars with different volume fractions of sands. The relationship between mortar pore structure and chloride ion diffusion coefficient was established to predict its chloride ion diffusion coefficient. It may provide a new idea for studying the durability of cement-based materials. Results indicated that similar to cement paste, the pore structure of mortar satisfied the fractal characteristics of solid phase within a certain range of pores. The most probable gel pore diameter of mortars with different sand volume fractions was about 4 nm, while the most probable capillary pore diameter was approximately 46 nm, and the critical pore diameter was ranging from 50 to 60 nm. MIP results indicated that with the increase in sand volume fraction (ϕagg), the total porosity (fmip) of the mortar decreased, satisfying the relationship of fmip = 0.1859 − 0.0789ϕagg. However, the porosity of the matrix (fbase) increased with the increase in sand volume fraction, which was due to the introduction of more interfaces by the addition of aggregates. The effective chloride ion diffusion coefficient (Dcp,base) of the matrix can be obtained by fitting. Based on this, the interface transition zone (ITZ) and the cement matrix were comprehensively considered as a whole fractal phase. The predicted value of the chloride ion diffusion coefficient obtained by the Mori–Tanaka homogenization method was in good agreement with the results obtained from rapid chloride migration (RCM) experiments, and the maximum error between the simulated and experimental values did not exceed 11%. This finding can provide new ideas for accurately predicting the chloride ion diffusion coefficient of mortar and even concrete. Full article
(This article belongs to the Special Issue Research on the Mechanical and Durability Properties of Concrete)
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<p>Pictures of raw materials. (<b>a</b>) Cement. (<b>b</b>) FA. (<b>c</b>) SF. (<b>d</b>) Sand.</p>
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<p>Pictures of RCM testing setup and specimen. (<b>a</b>) RCM testing setup. (<b>b</b>) Specimens.</p>
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<p>Analysis of MIP test results. (<b>a</b>) Pore sizes and cumulative mercury intrusion. (<b>b</b>) The relationship between solid fraction and pore size.</p>
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<p>Pore size distribution map of mercury injection.</p>
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<p>Pore distribution of NMR. (<b>a</b>) 4–6 nm peak. (<b>b</b>) 150–200 nm peak.</p>
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<p>Pore throat map of NMR.</p>
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<p>Pore size distribution of NAD. (<b>a</b>) 3–5 nm peak. (<b>b</b>) 40–60 nm peak.</p>
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<p>The comparison of porosity results obtained from MIP, NAD, and NMR. (<b>a</b>) comparison of porosity. (<b>b</b>) linear fitting.</p>
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<p>Normalized porosity of different Methods. (<b>a</b>) NAD. (<b>b</b>) NMR. (<b>c</b>) MIP.</p>
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<p>Comparison between MT model and experimental value.</p>
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19 pages, 1534 KiB  
Review
State of the Art of CFD-DEM Coupled Modeling and Its Application in Turbulent Flow-Induced Soil Erosion
by Jun Xu, Fei Wang and Ruth Abegaz
Geosciences 2025, 15(1), 21; https://doi.org/10.3390/geosciences15010021 - 10 Jan 2025
Viewed by 886
Abstract
Fluid–soil interaction plays a pivotal role in various geotechnical engineering applications, as it significantly influences processes such as erosion, sediment transport, and soil stability. Modeling fluid–soil particle interactions in these contexts presents substantial challenges due to the inherent complexity of the interactions occurring [...] Read more.
Fluid–soil interaction plays a pivotal role in various geotechnical engineering applications, as it significantly influences processes such as erosion, sediment transport, and soil stability. Modeling fluid–soil particle interactions in these contexts presents substantial challenges due to the inherent complexity of the interactions occurring across multiple characteristic scales. The primary challenge lies in the vast disparities in magnitude between these scales, which demand sophisticated modeling techniques to accurately capture the intricate dynamics involved. Coupled fluid–soil particle models have emerged as essential tools for understanding the mechanisms underlying fluid–soil interactions. Among these, the CFD-DEM (computational fluid dynamics–discrete element method) approach has gained significant attention. This method provides an effective compromise between high-resolution sub-particle fluid modeling and coarser mesh-based techniques for fluids and particles. By doing so, CFD-DEM facilitates large-scale simulations while maintaining computational efficiency, making it a promising solution for studying fluid–soil interactions in complex geotechnical scenarios. This review highlights the application of CFD-DEM models in geotechnical engineering, with a specific focus on soil erosion processes and the critical role of turbulent flow. It explores various fluid–soil particle interaction computational mechanisms and their implications for erosion dynamics, emphasizing several key aspects, including the following: laminar vs. turbulent flow models: understanding the distinctions between flow regimes is critical for accurately predicting fluid-induced soil particle movement. Shear stress effects: the influence of flow-induced shear stress on the detachment of soil particles is analyzed, particularly in erosion-prone environments. Sediment transport mechanisms: factors such as particle size, density, and water velocity are examined for their roles in governing sediment transport. Knowledge gaps and future directions: these involve identifying unresolved issues in current fluid–soil interaction models, with an emphasis on improving the accuracy and scalability of CFD-DEM simulations. By delving into these aspects, the review aims to advance the understanding of fluid–soil interactions and provide insights into optimizing modeling techniques for geotechnical engineering applications. It also outlines future research directions to bridge existing knowledge gaps, emphasizing the importance of integrating advanced turbulence modeling and computational strategies to enhance the predictive capabilities of fluid–soil interaction frameworks. Full article
(This article belongs to the Section Geomechanics)
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<p>Regions of the mesh–particle size ratio for resolved, semi-resolved, and unresolved CFD-DEM adopted from [<a href="#B89-geosciences-15-00021" class="html-bibr">89</a>,<a href="#B91-geosciences-15-00021" class="html-bibr">91</a>].</p>
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<p>Unresolved CFD-DEM models. The fluid drag force on particles was calculated using empirical models because the coarse mesh sizes were limited to resolve the forces on individual particles.</p>
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<p>Resolved CFD-DEM models. The fluid drag force on particles was calculated from fluid stresses on the particle surface due to the fine mesh sizes being able to resolve the forces on individual particles.</p>
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<p>Semi-resolved CFD-DEM models. The fluid drag force on particles was calculated from surrounding meshes using kernel functions. This coupling approach utilizes a kernel function to reconstruct the background information from all cells with centers within a specified smoothing distance, as shown in the red dashed circle, effectively eliminating dependency on grid size. This kernel-based approximation bridges the gap between CFD–DEM simulations using unresolved and resolved meshes, making it highly applicable to particulate flows with finer mesh sizes comparable to or slightly smaller than the particles themselves [<a href="#B92-geosciences-15-00021" class="html-bibr">92</a>].</p>
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<p>Forces and torques on a soil particle under flow.</p>
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19 pages, 15972 KiB  
Article
Eco-Friendly Stabilization of Physicochemically Dispersive Soil Using Sticky Rice and Calcium Chloride
by Zhuo Zhang, Henghui Fan, Jiangru Huo, Xingyu Zhang, Guanzhou Ren, Xiujuan Yang and Pengwei Wang
Sustainability 2025, 17(1), 182; https://doi.org/10.3390/su17010182 - 29 Dec 2024
Viewed by 872
Abstract
Dispersive soil is highly susceptible to water erosion, leading to significant engineering challenges, such as slope instability and canal damage. Common modifiers such as lime are effective but cause environmental pollution. Therefore, it is important to explore eco-friendly modifiers. This study investigates the [...] Read more.
Dispersive soil is highly susceptible to water erosion, leading to significant engineering challenges, such as slope instability and canal damage. Common modifiers such as lime are effective but cause environmental pollution. Therefore, it is important to explore eco-friendly modifiers. This study investigates the effects of sticky rice and calcium chloride (SRC) on dispersive soil. Dispersivity tests identified an optimal ratio of sticky rice to calcium chloride of 3:1. To analyze the effects of different SRC contents and curing times on the soil properties, tests of dispersivity, hydraulic, mechanical, chemical, and microscopic mechanisms were conducted based on this optimal ratio. The results indicated that 1.5% SRC effectively eliminated soil dispersivity even without curing, and its effectiveness improved with an extended curing time. After 28 days of curing, the water stability increased significantly, permeability decreased by an order of magnitude, and cohesion improved by approximately 85.97%. SRC reduced soil dispersivity through three primary mechanisms: lowering the pH, promoting ion exchange between Ca2+ and Na+, and the cementing effect of the sticky rice paste. Additionally, Ca2+ acted as a bridge between organic colloids and clay particles, further strengthening the structural stability of microaggregates. Overall, SRC proved to be an effective eco-friendly modifier for improving physicochemically dispersive soil. Full article
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<p>Photos showing the dispersivity results for the soil sample: (<b>a</b>) pinhole test—evaluates soil erosion and particle dispersion under water flow; (<b>b</b>) crumb test—assesses soil dispersivity based on the turbidity caused by dispersed particles in water.</p>
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<p>Experimental procedures.</p>
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<p>Disintegration test apparatus.</p>
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<p>Results of the dispersivity identification for soil treated with different ratios of SRC (sticky rice and CaCl<sub>2</sub>).</p>
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<p>Images of the dispersivity tests of soils treated with different SRC ratios: (<b>a</b>) cross-sectional images of soil samples after the pinhole test (with the water head indicated by WH) and (<b>b</b>) disintegration phenomena of soil samples (at the bottoms of the beakers).</p>
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<p>Images of the dispersivity tests of SRC-treated soil: (<b>a</b>) cross-sectional images of soil samples after the pinhole test (with the water head indicated by WH) and (<b>b</b>) disintegration phenomena of soil samples (at the bottoms of the beakers).</p>
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<p>Disintegration–time curves: (<b>a</b>) 0 days of curing; (<b>b</b>) 3 days of curing; (<b>c</b>) 7 days of curing; (<b>d</b>) 14 days of curing; and (<b>e</b>) 28 days of curing. (<b>f</b>) Average disintegration velocity.</p>
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<p>Disintegration–time curves: (<b>a</b>) 0 days of curing; (<b>b</b>) 3 days of curing; (<b>c</b>) 7 days of curing; (<b>d</b>) 14 days of curing; and (<b>e</b>) 28 days of curing. (<b>f</b>) Average disintegration velocity.</p>
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<p>Images of the disintegration test (9000 s) of SRC-treated soil with different contents after 7 days of curing: (<b>a</b>) 0.0%; (<b>b</b>) 0.5%; (<b>c</b>) 1.0%; (<b>d</b>) 1.5%; (<b>e</b>) 2.0%; and (<b>f</b>) 2.5%.</p>
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<p>Permeability coefficients of SRC-treated soil.</p>
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<p>Shear strength parameters of SRC-treated soil: (<b>a</b>) cohesion and (<b>b</b>) internal friction angle.</p>
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<p>pH and electrical conductivity of SRC-treated soil.</p>
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<p>Exchangeable sodium percentage of SRC-treated soil.</p>
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<p>SEM images and elemental maps: (<b>a</b>) dispersive soil (200×); (<b>b</b>) dispersive soil (1000×); (<b>c</b>) 1.5% SRC-treated soil (200×); (<b>d</b>) 1.5% SRC-treated soil (1000×); (<b>e</b>) 2.5% SRC-treated soil (200×); (<b>f</b>) 2.5% SRC-treated soil (1000×); (<b>g</b>) elemental map of dispersive soil; and (<b>h</b>) elemental map of 2.5% SRC-treated soil.</p>
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<p>SEM images and elemental maps: (<b>a</b>) dispersive soil (200×); (<b>b</b>) dispersive soil (1000×); (<b>c</b>) 1.5% SRC-treated soil (200×); (<b>d</b>) 1.5% SRC-treated soil (1000×); (<b>e</b>) 2.5% SRC-treated soil (200×); (<b>f</b>) 2.5% SRC-treated soil (1000×); (<b>g</b>) elemental map of dispersive soil; and (<b>h</b>) elemental map of 2.5% SRC-treated soil.</p>
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24 pages, 3114 KiB  
Article
Risk Perception in the Nigua River Basin: Key Determinants and Policy Implications
by Casimiro Maldonado-Santana, Antonio Torres-Valle, Carol Franco-Billini and Ulises Javier Jauregui-Haza
Water 2025, 17(1), 45; https://doi.org/10.3390/w17010045 - 27 Dec 2024
Viewed by 702
Abstract
The Nigua River basin in the Dominican Republic is a critical hydrographic area facing significant environmental challenges, including deforestation, soil erosion and pollution from mining and agricultural activities. This study explores the role of risk perception among local residents in shaping policies for [...] Read more.
The Nigua River basin in the Dominican Republic is a critical hydrographic area facing significant environmental challenges, including deforestation, soil erosion and pollution from mining and agricultural activities. This study explores the role of risk perception among local residents in shaping policies for the basin’s sustainable management. The research aims to identify the factors influencing risk perception and propose actionable strategies to improve environmental governance in the region. A “perceived risk profile” methodology was applied, using survey data from 1223 basin residents. The analysis identified key variables that influence risk perception, including demographic factors such as education, gender, and place of residence. The findings reveal that risk underestimation correlates with low awareness of risks, uncertainty about the origins of disasters, fatalism toward natural events, and low trust in institutions. In contrast, risk over-estimation is linked to infrequent risk communication, heightened catastrophism and a strong emphasis on the benefits of environmental protection. The study also highlights significant regional differences in risk perception, with residents of the lower basin exhibiting higher perceptions of risk due to cumulative pollution and frequent disaster impacts. Based on these insights, the study recommends targeted strategies to bridge risk perception gaps, including tailored risk communication, community-based environmental education and stronger institutional trust-building initiatives, all aimed at fostering more effective and inclusive environmental governance in the Nigua basin. Full article
(This article belongs to the Section Water Resources Management, Policy and Governance)
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<p>Geographic location of the Nigua hydrographic basin, Dominican Republic.</p>
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<p>Algorithm for risk perception study.</p>
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<p>Locations where the surveys were carried out (See <a href="#water-17-00045-t0A2" class="html-table">Table A2</a> in the <a href="#app1-water-17-00045" class="html-app">Appendix A</a>).</p>
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<p>Distribution of respondents according to place of residence and work in the Nigua basin.</p>
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<p>Perceived risk profile. (FAMI—Familiarity of the subject with the risk situation, UNDER—Risk understanding, UNCE—Uncertainty, WILL—Willfulness, INVO—Personal Involvement, CONT—Controllability, CATA—Catastrophic potential, HIST—Past history of disasters or dangers, IMME—Immediacy of consequences, REVE—Reversibility of consequences, PANI—Panic, R-IB—Risk-inequality benefit, BENE—Expected benefits of exposure, INST—Trust in institutions, PRES—Role of the press or broadcast media). The dimensionless risk perception scale (Y axis) indicates: 1–risk underestimation; 2–adequate estimation of the risk; 3–risk overestimation.</p>
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<p>Comparison of risk perception by sex. (FAMI—Familiarity of the subject with the risk situation, UNDER—Risk understanding, UNCE—Uncertainty, WILL—Willfulness, INVO-Personal Involvement, CONT—Controllability, CATA—Catastrophic potential, HIST—Past history of disasters or dangers, IMME—Immediacy of consequences, REVE-Reversibility of consequences, PANI—Panic, R-IB—Risk-inequality benefit, BENE—Expected benefits of exposure, INST—Trust in institutions, PRES—Role of the press or broadcast media). The dimensionless risk perception scale (Y axis) indicates: 1–risk underestimation; 2–adequate estimation of the risk; 3–risk overestimation.</p>
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<p>Comparison of risk perception by age. (FAMI—Familiarity of the subject with the risk situation, UNDER—Risk understanding, UNCE—Uncertainty, WILL—Willfulness, INVO—Personal Involvement, CONT—Controllability, CATA—Catastrophic potential, HIST—- Past history of disasters or dangers, IMME—Immediacy of consequences, REVE—Reversibility of consequences, PANI—Panic, R-IB—Risk-inequality benefit, BENE—Expected benefits of exposure, INST—Trust in institutions, PRES—Role of the press or broadcast media). The dimensionless risk perception scale (Y axis) indicates: 1–risk underestimation; 2–adequate estimation of the risk; 3–risk overestimation.</p>
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<p>Comparison of risk perception by place of residence. (FAMI—Familiarity of the subject with the risk situation, UNDER—Risk understanding, UNCE—Uncertainty, WILL—Willfulness, INVO—Personal Involvement, CONT—Controllability, CATA—Catastrophic potential, HIST—Past history of disasters or dangers, IMME—Immediacy of consequences, REVE—Reversibility of consequences, PANI—Panic, R-IB—Risk-inequality benefit, BENE—Expected benefits of exposure, INST—Trust in institutions, PRES—Role of the press or broadcast media). The dimensionless risk perception scale (Y axis) indicates: 1–risk underestimation; 2–adequate estimation of the risk; 3–risk overestimation.</p>
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<p>Comparison of risk perception by education. (FAMI—Familiarity of the subject with the risk situation, UNDER—Risk understanding, UNCE—Uncertainty, WILL—Willfulness, INVO—Personal Involvement, CONT—Controllability, CATA—Catastrophic potential, HIST—Past history of disasters or dangers, IMME—Immediacy of consequences, REVE—Reversibility of consequences, PANI—Panic, R-IB—Risk-inequality benefit, BENE—Expected benefits of exposure, INST—Trust in institutions, PRES—Role of the press or broadcast media). The dimensionless risk perception scale (Y axis) indicates: 1–risk underestimation; 2–adequate estimation of the risk; 3–risk overestimation.</p>
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14 pages, 17158 KiB  
Article
In Situ Testing and Finite Element Analysis of a Discontinuous Mortise and Tenon Stone Bridge Under Natural Excitation
by Jiaxing Hu, Shilong Wang, Ming Sun and Ji Zhou
Buildings 2024, 14(11), 3596; https://doi.org/10.3390/buildings14113596 - 12 Nov 2024
Viewed by 733
Abstract
To study the dynamic response of multi-span mortise and tenon stone bridges under natural excitation, a bluestone multi-span stone bridge with a main span of 2.56 m in southern China was taken as the research object. Based on the collected pulsating signals of [...] Read more.
To study the dynamic response of multi-span mortise and tenon stone bridges under natural excitation, a bluestone multi-span stone bridge with a main span of 2.56 m in southern China was taken as the research object. Based on the collected pulsating signals of bridge piers and slabs, the natural frequencies and damping ratios of the main span bridge slab and pier were analyzed using the half-power broadband method (HPBM) and random decrement technique (RDT). Modal analysis was conducted using ANSYS, and the results were compared with those obtained from on-site experiments for further performance analysis. The research results of this article indicate that the natural frequency range of the 2.56-m bridge slab identified by measured signals is 48–49 Hz, and the damping ratio range is 33.33–36.61%. The natural frequency of the central pier is 75–76 Hz, and the damping ratio range is 26.39–27.83%. Through finite element modal analysis, the natural frequency of the bridge slab is 54.401 Hz, with an error of 10.5%. The natural frequency of the overall stone bridge is about 82.2 Hz, with an error of about 8.2%. The validated finite element model was subjected to normal water flow impact and erosion simulation. The results indicate that under erosion with fewer particles and lower flow rates, the upstream pier bottom at the center receives the highest relative erosion mass and displacement per unit area. The bridge deck near the main span also experienced relative displacement. Therefore, in the subsequent protection work, special attention should be paid to these components. Full article
(This article belongs to the Section Building Structures)
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<p>Ancient Stone Bridge. (<b>a</b>) Mortise and tenon stone bridge; (<b>b</b>) Plan of Stone Bridge slabs; (<b>c</b>) Elevation of Stone Bridge.</p>
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<p>Sensor arrangement.</p>
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<p>Test equipment on site. (<b>a</b>) YZKJ-DIAK dynamic signal acquisition system; (<b>b</b>) 991B accelerometer; (<b>c</b>) a computer for processing.</p>
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<p>Acceleration response time history.</p>
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<p>Attenuation fitting curve of Bridge slab.</p>
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<p>Attenuation fitting curve of Bridge pier.</p>
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<p>Comparison diagram of Bridge slab.</p>
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<p>Comparison diagram of Bridge pier.</p>
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<p>Comparison of boundary conditions. (<b>a</b>) Explanation of Actual Boundary Conditions for stone bridge; (<b>b</b>) Schematic diagram of boundary conditions for stone bridge model.</p>
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<p>Vibration mode diagram. (<b>a</b>) Bridge slab Vibration Mode Diagram; (<b>b</b>) Vibration mode diagram of a stone bridge with a friction coefficient of 0.6; (<b>c</b>) Vibration mode diagram of a stone bridge with a friction coefficient of 0.8.</p>
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<p>Computational Domain Model.</p>
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<p>Bridge pier erosion cloud map.</p>
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<p>Diagram of Static Analysis of Stone Bridge. (<b>a</b>) Erosion plan; (<b>b</b>) Flow pressure distribution diagram; (<b>c</b>) Displacement diagram of stone bridge under flowing water impact.</p>
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20 pages, 12022 KiB  
Article
Study on the Effect of Basalt Fiber Content and Length on Mechanical Properties and Durability of Coal Gangue Concrete
by Zixin He, Xiao Zhao, Meichen Ye, Wei Zuo, Xiaoxiong Nie and Jianjun Zhao
Sustainability 2024, 16(21), 9310; https://doi.org/10.3390/su16219310 - 26 Oct 2024
Cited by 1 | Viewed by 1159
Abstract
The massive accumulation of coal gangue not only causes a waste of resources but also brings serious environmental pollution problems. To promote the utilization of coal gangue resources, mitigate environmental pollution from coal gangue, and address the shortage of natural aggregates, this study [...] Read more.
The massive accumulation of coal gangue not only causes a waste of resources but also brings serious environmental pollution problems. To promote the utilization of coal gangue resources, mitigate environmental pollution from coal gangue, and address the shortage of natural aggregates, this study investigates the use of coal gangue to replace coarse aggregate at a 40% replacement rate to prepare coal gangue concrete (CGC). The current research on the modification of gangue concrete by BF has been less often compared with the research on the effect of basalt fiber (BF) on the properties of ordinary concrete, so in this study, BF with different admixtures and lengths were added into CGC. Additionally, basalt fibers (BFs) of varying amounts and lengths were incorporated into CGC. The study explored the effects of BF on the tensile strength, splitting tensile strength, and flexural strength of CGC. It was found that the mechanical properties of CGC improved significantly when the BF dosage was 0.10–0.15% and the length was 18 mm. This is evidenced by an increase in the compressive strength of 3.94–5.11%, split tensile strength of 11.20–16.18%, and flexural strength of 8.23–12.97%. BF was able to refine pore space, prevent crack development, and bridge cracks in CGC. To further investigate the effect of BF on the long-term service performance of CGC, the effects of BF on the appearance, quality, and compressive strength of CGC in sulfate and freeze–thaw environments were examined. The results indicated that a BF dosage of 0.10–0.15% significantly enhanced the sulfate erosion resistance and freeze–thaw resistance of CGC. This is shown by a 36.76–46.90% reduction in the rate of loss of compressive strength of CGC under the freeze–thaw cycling and a 6.21–8.50% increase in the corrosion resistance factor of CGC under a sulfate attack. BF improved the pore structure and reduced seepage channels, thereby enhancing the durability of CGC. Full article
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<p>(<b>a</b>) Gangue aggregate; (<b>b</b>) natural aggregate.</p>
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<p>(<b>a</b>) Cement; (<b>b</b>) silica fume.</p>
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<p>Basalt fiber diagram.</p>
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<p>Schematic diagram of specimen preparation.</p>
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<p>Sample preparation flowchart.</p>
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<p>(<b>a</b>) Compressive test, (<b>b</b>) splitting tensile test, and (<b>c</b>) flexural test.</p>
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<p>(<b>a</b>) Compressive test, (<b>b</b>) splitting tensile test, and (<b>c</b>) flexural test.</p>
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<p>(<b>a</b>) Effect of BF length on the compressive strength of CGC; (<b>b</b>) Effect of BF content on CGC compressive strength.</p>
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<p>CGC compressive damage patterns: (<b>a</b>) B0; (<b>b</b>) D3; (<b>c</b>) D4.</p>
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<p>(<b>a</b>) Effect of BF length on CGC splitting tensile strength; (<b>b</b>) effect of BF content on CGC splitting tensile strength.</p>
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<p>CGC split tensile damage patterns: (<b>a</b>) B0; (<b>b</b>) D3; (<b>c</b>) D4.</p>
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<p>(<b>a</b>) Effect of BF length on flexural strength of CGC; (<b>b</b>) effect of BF content on flexural strength of CGC.</p>
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<p>CGC flexural strength damage patterns: (<b>a</b>) B0; (<b>b</b>) D3; (<b>c</b>) D4.</p>
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<p>Rate of mass loss of CGC after freeze–thaw cycles.</p>
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<p>Changes in compressive strength of CGC after freeze–thaw cycles.</p>
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<p>Rate of quality loss after sulfate attack.</p>
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<p>Changes in compressive strength of concrete after sulfate attack.</p>
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<p>Mechanism diagram of BF on CGC sulfate erosion.</p>
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<p>(<b>a</b>) Fibers in close contact with the cement matrix; (<b>b</b>) fibers embedded within the cement matrix; (<b>c</b>) randomly distributed fibers; (<b>d</b>) fiber agglomerates.</p>
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<p>(<b>a</b>) Fibers in close contact with the cement matrix; (<b>b</b>) fibers embedded within the cement matrix; (<b>c</b>) randomly distributed fibers; (<b>d</b>) fiber agglomerates.</p>
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<p>(<b>a</b>) Basalt fiber to fill pores; (<b>b</b>) basalt fiber to resist cracking; (<b>c</b>) basalt fiber to fracture for toughening.</p>
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<p>Schematic diagram of basalt fiber toughening.</p>
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18 pages, 10702 KiB  
Article
Prediction of Scour Depth for Diverse Pier Shapes Utilizing Two-Dimensional Hydraulic Engineering Center’s River Analysis System Sediment Model
by Muhanad Al-Jubouri, Richard P. Ray and Ethar H. Abbas
Fluids 2024, 9(11), 247; https://doi.org/10.3390/fluids9110247 - 25 Oct 2024
Cited by 1 | Viewed by 913
Abstract
Examining scouring around bridge piers is crucial for ensuring water-related infrastructure’s long-term safety and stability. Accurate forecasting models are essential for addressing scour, especially in complex water systems where traditional methods fall short. This study investigates the application of the HEC-RAS 2D sedimentation [...] Read more.
Examining scouring around bridge piers is crucial for ensuring water-related infrastructure’s long-term safety and stability. Accurate forecasting models are essential for addressing scour, especially in complex water systems where traditional methods fall short. This study investigates the application of the HEC-RAS 2D sedimentation model, which has recently become available for detailed sediment analysis, to evaluate its effectiveness in predicting scoring around various pier shapes and under different water conditions. This study offers a comprehensive assessment of the model’s predictive capabilities by focusing on variables such as water velocity, shear stress, and riverbed changes. Particular attention was paid to the influence of factors like floating debris and different pier geometries on scour predictions. The results demonstrate that while the HEC-RAS 2D model generally provides accurate predictions for simpler pier shapes—achieving up to 85% precision—it shows varied performance for more complex designs and debris-influenced scenarios. Specifically, the model overpredicted scouring depths by approximately 20% for diamond-shaped piers and underpredicted by 15% for square piers in debris conditions. Elliptical piers, in contrast, experienced significantly less erosion, with scour depths up to 30% shallower compared to other shapes. This study highlights the novel application of the HEC-RAS 2D model in this context and underscores its strengths and limitations. Identified issues include difficulties in modeling water flow and debris-induced bottlenecks. This research points to the improved calibration of sediment movement parameters and the development of advanced computational techniques to enhance scour prediction accuracy in complex environments. This work contributes valuable insights for future research and practical applications in civil engineering, especially where traditional scour mitigation methods, such as apron coverings, are not feasible. Full article
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<p>(<b>a</b>) Experimental flume setup for analyzing local scour around a cylindrical pier with rectangular debris, and (<b>b</b>) centerline and longitudinal profile lines used for scour depth analysis.</p>
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<p>Visual representation of rectangular flume with diamond pier: (<b>a</b>) top view 2D terrain model and (<b>b</b>) RAS 3-D viewer showing the velocity distribution around the pier.</p>
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<p>Flowchart of the methodology applied in the 2D HEC-RAS model approach.</p>
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<p>Calibration of grid size based on flow water depth and velocity, showing how grid resolution impacts simulation accuracy.</p>
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<p>Calibration of the Manning coefficient (n) based on variations in flow water depth and velocity.</p>
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<p>Velocity distribution patterns around different pier designs, showing the flow behavior and areas of acceleration and recirculation for each geometry.</p>
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<p>Hydraulic conditions around piers, showing velocity distribution, flow depth, and bed shear stress for (<b>a</b>) diamond-shaped pier and (<b>b</b>) elliptical-shaped pier.</p>
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<p>Bed level changes around piers from top and front views, including (<b>a</b>) cylindrical, (<b>b</b>) square, (<b>c</b>) rectangular, (<b>d</b>) diamond, (<b>e</b>) oval, (<b>f</b>) ogival, and (<b>g</b>) elliptical pier designs.</p>
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<p>Bed level changes around piers from top and front views, including (<b>a</b>) cylindrical, (<b>b</b>) square, (<b>c</b>) rectangular, (<b>d</b>) diamond, (<b>e</b>) oval, (<b>f</b>) ogival, and (<b>g</b>) elliptical pier designs.</p>
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<p>Bed level changes around piers from top and front views, including (<b>a</b>) cylindrical, (<b>b</b>) square, (<b>c</b>) rectangular, (<b>d</b>) diamond, (<b>e</b>) oval, (<b>f</b>) ogival, and (<b>g</b>) elliptical pier designs.</p>
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<p>Comparison of experimental and 2D HEC-RAS sediment model results for scour depth around various pier designs.</p>
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<p>Variation in bed level around a cylindrical pier due to various debris configurations, detailed as follows: (<b>a</b>) no debris, D = 2.5 cm; (<b>b</b>) rectangle and triangle debris, T/Y = 0.25, De = 3.74 cm; (<b>c</b>) rectangle and triangle debris, T/Y = 0.5, De = 4.97 cm; (<b>d</b>) rectangle debris, T/Y = 0.25, a = 3.43 cm; (<b>e</b>) rectangle debris, T/Y = 0.5, a = 4.35 cm; (<b>f</b>) triangle debris, T/Y = 0.25, a = 2.83 cm; (<b>g</b>) triangle debris, T/Y = 0.5, a = 3.17 cm.</p>
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17 pages, 11316 KiB  
Article
Experimental Study on the Flexural Performance of the Corrosion-Affected Simply Supported Prestressed Concrete Box Girder in a High-Speed Railway
by Hai Li, Yuanguang Qiu, Zhicheng Pan, Yiming Yang, Huang Tang and Fanjun Ma
Buildings 2024, 14(10), 3322; https://doi.org/10.3390/buildings14103322 - 21 Oct 2024
Viewed by 716
Abstract
Prestressed concrete box girders are commonly employed in the development of high-speed railway bridge constructions. The prestressed strands in the girder may corrode due to long-term chloride erosion, leading to the degradation of its flexural performance. To examine the flexural performance of corrosion-affected [...] Read more.
Prestressed concrete box girders are commonly employed in the development of high-speed railway bridge constructions. The prestressed strands in the girder may corrode due to long-term chloride erosion, leading to the degradation of its flexural performance. To examine the flexural performance of corrosion-affected simply supported prestressed concrete box girders, eight T-shaped mock-up beams related to the girders used in the construction of high-speed railway bridges were manufactured utilizing similarity theory. Seven of the beams underwent electrochemical accelerated corrosion, and then each beam was subjected to failure under the four-point load test method. Measurements recorded and analyzed in detail during the loading process included the following: crack propagation, crack width at various loads, crack load, ultimate load, deflection, and concrete strain of the mid-span section. The results demonstrate that a corrosion rate of just 8.31% has a considerable impact on the structural integrity of the beams, as evidenced by a pronounced reduction in flexural cracks and a tendency towards reduced reinforcement failure. Furthermore, the corrosive process has a detrimental effect on mid-span deflection, ductility, and ultimate flexural bearing capacity, which could have significant implications for bridge safety. This study provides valuable insights for the assessment of flexural performance and the development of appropriate maintenance strategies for corroded simply supported box girders in high-speed railways. Full article
(This article belongs to the Section Building Structures)
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<p>Cross-section of model T-shaped beam (mm).</p>
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<p>Schematic of model T-shaped beam (mm).</p>
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<p>Reinforcement diagram of model T-shaped beam (mm).</p>
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<p>Accelerated corrosion process of specimens.</p>
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<p>A diagram illustrating the loading arrangement.</p>
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<p>Test site with loading and measurement devices.</p>
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<p>Failure patterns of the test beams.</p>
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<p>Failure patterns of the test beams.</p>
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<p>Final crack distribution of test beams.</p>
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<p>Final crack distribution of test beams.</p>
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<p>Moment–deflection response of mid-span deflection.</p>
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<p>Moment–deflection response of mid-span deflection.</p>
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<p>Moment–concrete strain curve at mid-span section.</p>
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<p>Moment–concrete strain curve at mid-span section.</p>
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<p>Flexural bearing capacity versus the corrosion rate of the steel strand.</p>
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<p>Relationship between the decrease rate of the flexural bearing capacity and the corrosion rate of the steel strand.</p>
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21 pages, 15978 KiB  
Article
Attenuation Law of Performance of Concrete Anti-Corrosion Coating under Long-Term Salt Corrosion
by Tao Fan, Yongchang Wu, Mingda Yang, Peng Xu, Yongqing Li, Laifa Wang and Huaxin Chen
Coatings 2024, 14(10), 1249; https://doi.org/10.3390/coatings14101249 - 30 Sep 2024
Viewed by 1063
Abstract
In saline soil areas, the concrete piers of concrete bridges experience long-term corrosion, mainly caused by chloride salts due to alternating temperature changes. Waterborne concrete coatings are prone to failure in this aggressive salt environment. Implementing coating protection measures can improve the durability [...] Read more.
In saline soil areas, the concrete piers of concrete bridges experience long-term corrosion, mainly caused by chloride salts due to alternating temperature changes. Waterborne concrete coatings are prone to failure in this aggressive salt environment. Implementing coating protection measures can improve the durability of concrete and enhance the service life of bridges. However, the effectiveness and longevity of coatings need further research. In this paper, three types of waterborne concrete anti-corrosion coatings were applied to analyze the macro and micro surface morphology under wet–dry cycles and long-term immersion conditions. Various indicators such as glossiness, color difference, and adhesion of the coatings were tested during different cyclic periods. The chloride ion distribution characteristics of the buried concrete coatings in saline soil, the macro morphology analysis of chloride ion distribution regions, and the micro morphology changes of the coatings under different corrosion times were also investigated. The results showed that waterborne epoxy coatings (ES), waterborne fluorocarbon coatings (FS), and waterborne acrylic coatings (AS) all gradually failed under long-term salt exposure, with increasing coating porosity, loss of internal fillers, and delamination. The chloride ion content inside the concrete decreased with increasing depth at the same corrosion time, while the chloride ion content at the same depth increased with time. The chloride ion distribution boundary in the cross-section of concrete with coating protection was not significant, while the chloride ion distribution boundary in the cross-section of untreated concrete gradually contracted towards the concrete core with increasing corrosion time. During the corrosion process in saline soil, the coatings underwent three stages: adherence of small saline soil particles, continuous increase in adhered material area, and multiple layers of uneven coverage by saline soil. The failure process of the coatings still required erosive ions to infiltrate the surface through micropores. The predicted lifespans of FS, ES, and AS coatings, obtained through weighted methods, were 2.45 years, 2.48 years, and 2.74 years, respectively, which were close to the actual lifespans observed in salt environments. The developed formulas effectively reflect the corrosion patterns of different resin-based coatings under salt exposure, providing a basis for accurately assessing the corrosion behavior and protective effectiveness of concrete under actual environmental factors. Full article
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<p>Salt content corrosion test signal.</p>
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<p>Wet–dry cycle test device.</p>
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<p>Drilling point location and depth distribution.</p>
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<p>Coating bond strength test.</p>
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<p>Macromorphological changes of waterborne fluorocarbon coating at different durations of wet–dry cycling.</p>
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<p>Macromorphological changes of waterborne epoxy coating at different durations of wet–dry cycling.</p>
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<p>Macromorphological changes of waterborne acrylic coating at different durations of wet–dry cycling.</p>
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<p>Microscopic morphological changes (SEM) of waterborne fluorocarbon coatings.</p>
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<p>Microscopic morphological changes (SEM) of waterborne epoxy coatings.</p>
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<p>Microscopic morphological changes (SEM) of waterborne acrylic coatings.</p>
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<p>Discolor boundary of coating protective concrete test block section for 36 days.</p>
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<p>Discolor boundary of coating protective concrete test block section for 90 days.</p>
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<p>Discolor boundary of coating protective concrete test block section for 180 days.</p>
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<p>Discolor boundary of coating protective concrete test block section for 270 days.</p>
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<p>Microtopography of FS coating at different salt corrosion times.</p>
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<p>Microtopography of ES coating at different salt corrosion times.</p>
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<p>Microtopography of AS coating at different salt corrosion times.</p>
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<p>Changes in glossiness of FS, ES, and AS coatings.</p>
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<p>Changes in color difference values of FS, ES, and AS coatings.</p>
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<p>Changes in adhesion of FS, ES, and AS coatings.</p>
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<p>Different depth chloride content in concrete for coating protection.</p>
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<p>Fitting curve of coating loss rate with time (FS, ES, AS coatings from left to right).</p>
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<p>Fitting curve of coating color difference value with time (FS, ES, and AS coatings from left to right).</p>
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<p>Fitting curve of coating adhesion and time (FS, ES, and AS coatings from left to right).</p>
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13 pages, 9816 KiB  
Article
Sustainable Utilization of Stabilized Dredged Material for Coastal Infrastructure: Innovations in Non-Fired Brick Production and Erosion Control
by Thi Thuy Minh Nguyen, Saeed Rabbanifar, Aalok Sharma Kafle, Reid Johnson, Brian Bonner, Dason Fernandez, Fernando Aleman, Jared Defrancis, Chun-Wei Yao, Xianchang Li, Mien Jao and Paul Bernazzani
Appl. Sci. 2024, 14(18), 8544; https://doi.org/10.3390/app14188544 - 23 Sep 2024
Viewed by 1059
Abstract
The deterioration of dams and levees is an increasing concern for both infrastructure integrity and environmental sustainability. The extensive repercussions, including the displacement of communities, underscore the imperative for sustainable interventions. This study addresses these challenges by investigating the stabilization of dredged material [...] Read more.
The deterioration of dams and levees is an increasing concern for both infrastructure integrity and environmental sustainability. The extensive repercussions, including the displacement of communities, underscore the imperative for sustainable interventions. This study addresses these challenges by investigating the stabilization of dredged material (DM) for diverse applications. Seven mixtures incorporating fly ash, lime, and cement were formulated. The Standard Compaction Test was used to determine optimal density–moisture conditions, which helped with brick fabrication. Bricks were tested for compressive strength over various curing periods, and the durability of the 28-day-cured samples was evaluated by performing water immersion tests following the New Mexico Code specifications. Scanning electron microscopy (SEM) was used to assess microstructural bonding. Results confirm that the inclusion of cementitious stabilizers modifies the material’s microstructure, resulting in enhancements of both strength and water resistance. Notably, the stabilized material demonstrates potential for use in non-fired brick manufacturing and as bridge stones for waterway erosion control. This dual-function application offers a sustainable and economically feasible approach to managing dredged materials. Full article
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<p>Location overview of Placement Area 9 (PA9): (<b>A</b>) a GIS map highlighting the location of PA9 within Texas; (<b>B</b>) a detailed GIS map showing the boundaries of PA9; (<b>C</b>) an aerial photograph depicting the surrounding area of PA9; (<b>D</b>) an aerial photograph providing a close-up view of PA9.</p>
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<p>The brick fabrication process involves the drying of DM and the mixing of additives (panel (<b>A</b>)), the ensuring of proper moisture content (panel (<b>B</b>)), and the use of the Auram Press 3000 to make the compressed bricks (panel (<b>C</b>)). The final results: a series of bricks (panel (<b>D</b>)).</p>
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<p>Image of a typical compressed block from stabilized dredged material using mix design 4 (HL/FA/PC ratio of 35/80.5/10).</p>
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<p>Particle size distribution of DM and additives.</p>
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<p>Compaction data for varying contents of HL and FA (for PC = 10%).</p>
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<p>Compaction data for varying contents of HL and FA (for PC = 15%).</p>
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<p>Stabilized mixed at a fixed dosage of HL and FA (for PC = 10, 15, and 20).</p>
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<p>UCS of all stabilized samples.</p>
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<p>Scanning electron microscopy (SEM) image 1000x magnification of (<b>A</b>) fly ash and (<b>B</b>) hydrated lime. The yellow arrows indicate the presence of voids.</p>
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<p>SEM images of the highest dosage (35/84.5/20) at different scales: (<b>A</b>) 1000x highlighting the enveloping of small particles; (<b>B</b>) 1000x highlighting the continuous smooth texture; (<b>C</b>) 2000x, and (<b>D</b>) 3000x. The white arrows highlight the presence of excess fly ash material.</p>
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15 pages, 10315 KiB  
Article
Corrosion Behaviors of Weathering Steels in the Actual Marine Atmospheric Zone and Immersion Zone
by Ying Yang, Tianzi Lin, Guohui Wang, Yubo Wang, Minghui Shao, Fandi Meng and Fuhui Wang
Metals 2024, 14(8), 903; https://doi.org/10.3390/met14080903 - 9 Aug 2024
Cited by 2 | Viewed by 1699
Abstract
The corrosion behaviors of three bridge steels in a real tropical marine environment for 2 years were studied. One weathering steel (WS) was designed with higher levels of nickel, copper, and molybdenum compared to the other. These two kinds of WSs and one [...] Read more.
The corrosion behaviors of three bridge steels in a real tropical marine environment for 2 years were studied. One weathering steel (WS) was designed with higher levels of nickel, copper, and molybdenum compared to the other. These two kinds of WSs and one kind of ordinary high-strength low-alloy steel (Q345qe) were compared under two conditions (marine atmospheric zone and marine immersion zone at Sanya Marine Environmental Test Station). The morphology, corrosion rate, and corrosion product analysis of the steels were performed through SEM, XPS, FTIR and other characterization methods. The results demonstrated that weathering steels facilitate the densification of the corrosion product layer due to the addition of alloying elements Cr, Ni, and Cu, promoting rust nucleation and enhancing the compactness of the protective layer. However, in an immersion environment, the extensive erosion by chloride ions renders the benefits of WS ineffective. Full article
(This article belongs to the Special Issue Corrosion of Metals: Behaviors and Mechanisms)
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<p>Climatic data during the exposure period at Sanya station: (<b>a</b>) the average temperature for each month; (<b>b</b>) the average relative humidity for each month. Photos of the corrosion test equipment and samples in the (<b>c</b>) marine atmospheric zone and (<b>d</b>) marine immersion zone. (<b>e</b>) Schematic diagram of the size of the samples.</p>
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<p>Metallographic structure of bridge steels: (<b>a</b>) #1 steel; (<b>b</b>) #2 steel; and (<b>c</b>) #3 steel.</p>
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<p>Mass changes and corrosion rates of the three steels at different time points for (<b>a</b>,<b>b</b>) atmospheric zone and (<b>c</b>,<b>d</b>) immersion zone.</p>
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<p>Corrosion depths of the three steels after two years for (<b>a</b>) atmospheric zone and (<b>b</b>) immersion zone.</p>
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<p>Macroscopic corrosion morphology of three kinds of steels at different time points for (<b>a</b>) atmospheric zone and (<b>b</b>) immersion zone.</p>
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<p>Morphology of substrates after complete removal of rust for (<b>a</b>) atmospheric zone and (<b>b</b>) immersion zone.</p>
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<p>Morphology of substrates after complete removal of rust for (<b>a</b>) atmospheric zone and (<b>b</b>) immersion zone.</p>
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<p>Microscopic corrosion morphology of 1# steel in atmospheric zone at different times: (<b>a</b>,<b>b</b>) 0.5 years and its high magnification micrograph; (<b>c</b>,<b>d</b>) 1 year and its high magnification micrograph with the feature of clustered corrosion products (red plus sign); (<b>e</b>,<b>f</b>) 1.5 years and its high magnification micrograph; (<b>g</b>,<b>h</b>) 2 years and its high magnification micrograph.</p>
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<p>Microscopic corrosion morphology of 2# steel in atmospheric zone at different times: (<b>a</b>,<b>b</b>) 0.5 years and its high magnification micrograph; (<b>c</b>,<b>d</b>) 1 year and its high magnification micrograph with the feature of rod clustered corrosion products (red plus sign); (<b>e</b>,<b>f</b>) 1.5 years and its high magnification micrograph; (<b>g</b>,<b>h</b>) 2 years and its high magnification micrograph.</p>
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<p>Microscopic corrosion morphology of 3# steel in atmospheric zone at different times: (<b>a</b>,<b>b</b>) 0.5 years and its high magnification micrograph; (<b>c</b>,<b>d</b>) 1 year and its high magnification micrograph with the feature of needle-like corrosion products (red plus sign); (<b>e</b>,<b>f</b>) 1.5 years and its high magnification micrograph; (<b>g</b>,<b>h</b>) 2 years and its high magnification micrograph.</p>
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<p>Microscopic corrosion morphology of 1# steel in immersion zone at different times: (<b>a</b>,<b>b</b>) 0.5 years and its high magnification micrograph; (<b>c</b>,<b>d</b>) 1 year and its high magnification micrograph with the feature of spherical corrosion products (red plus sign); (<b>e</b>,<b>f</b>) 1.5 years and its high magnification micrograph; (<b>g</b>,<b>h</b>) 2 years and its high magnification micrograph.</p>
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<p>Microscopic corrosion morphology of 2# steel in immersion zone at different times: (<b>a</b>,<b>b</b>) 0.5 years and its high magnification micrograph; (<b>c</b>,<b>d</b>) 1 year and its high magnification micrograph with the feature of fine needles corrosion products (red plus sign); (<b>e</b>,<b>f</b>) 1.5 years and its high magnification micrograph; (<b>g</b>,<b>h</b>) 2 years and its high magnification micrograph.</p>
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<p>Microscopic corrosion morphology of 3# steel in immersion zone at different times: (<b>a</b>,<b>b</b>) 0.5 years and its high magnification micrograph; (<b>c</b>,<b>d</b>) 1 year and its high magnification micrograph with the feature of blocky and strip-like corrosion products (red plus sign); (<b>e</b>,<b>f</b>) 1.5 years and its high magnification micrograph; (<b>g</b>,<b>h</b>) 2 years and its high magnification micrograph.</p>
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<p>XRD results of the corrosion products of steels exposed to the marine atmospheric environment for 0.5 years.</p>
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<p>FTIR results of different steels in the atmospheric zone after 2 years.</p>
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<p>XRD results of the corrosion products of steels immersed in the marine immersion zone for 0.5 years.</p>
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<p>FTIR results of different steels in the immersion zone after 2 years.</p>
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17 pages, 15832 KiB  
Article
Development of Indicator for Piled Pier Health Evaluation in Vietnam Using Impact Vibration Test Approach
by Thi Bach Duong Nguyen, Jungwon Huh, Thanh Thai Vu, Minh Long Tran and Van Ha Mac
Buildings 2024, 14(8), 2366; https://doi.org/10.3390/buildings14082366 - 1 Aug 2024
Viewed by 1368
Abstract
Vietnam’s seaport system currently includes 298 ports with 588 wharves (a total length of approximately 92,275 m), which is vital in developing Vietnam’s marine economy. The piled pier, a type of wharf structure, is widely used and accounts for up to 90%, while [...] Read more.
Vietnam’s seaport system currently includes 298 ports with 588 wharves (a total length of approximately 92,275 m), which is vital in developing Vietnam’s marine economy. The piled pier, a type of wharf structure, is widely used and accounts for up to 90%, while the remaining 10% is made up of other types of wharf structures, such as gravity and sheet pile quay walls. Most wharves have been operating for over 10 years and some for even more than 50 years. Noticeably, wharves are highly vulnerable and degrade rapidly due to many factors, especially heavy load impacts and severe environmental conditions. Additionally, wharves have a higher risk of deterioration than other inland infrastructure, such as buildings and bridges. Consequently, determining a wharf’s health is an important task in maintaining normal working conditions, extending its lifecycle, and avoiding other severe damage that could lead to dangers to the safety of vehicles, facilities, and humans. Moreover, regulated quality inspections usually include only simple inspections, e.g., displacement, settlement, geometric height, and tilt; the visual inspection and determination of dimensions by simple length-measuring equipment; concrete strength testing by ultrasonic and rebound hammers; and the experimental identification of the chloride ion concentration, chloride diffusion coefficient, corrosion activity of rebar in concrete, and steel thickness. These testing methods often give local results depending on the number of test samples. Therefore, advanced diagnostic techniques for assessing the technical condition of piled piers need to be studied. The impact vibration test (IVT) is a powerful non-destructive evaluation method that indicates the overall health of structures, e.g., underground and foundation structures, according to official standards. Hence, the IVT is expected to help engineers detect the potential deterioration of overall structures. It is fundamental that, if a structure is degraded, its natural frequency will be affected. A structure’s health index and technical condition are determined based on this change. However, the IVT does not seem to be widely applied to piled piers, with no published standard; hence, controversial issues related to accuracy and reliability still remain. This motivates the present study to recommend an adjusted factor (equal to 1.16) for the health index (classified in official standards for other structures) through numerical and experimental approaches before officially applying the IVT method to piled piers. The current work focuses on the health index using the design natural frequency, which is more practical in common cases where previous historical data and the standard natural frequency are unavailable. This study also examines a huge number of influencing factors and situations through theoretical analysis, experience, and field experiments to propose an adjusted indicator. The results are achieved with several assumptions of damages, such as the degradation of materials and local damages to structural components. With the proposed adjusted indicator, the overall health of piled piers can be assessed quickly and accurately by IVT inspections in cases of incidents, accidents due to collisions, cargo falls during loading and unloading, or subsidence and erosion due to natural disasters, storms, and floods. Full article
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<p>Arrangement of filed IVT experiments for several ports.</p>
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<p>Procedure for assessing the health status of piled piers in the IVT method.</p>
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<p>Providing horizontal impact forces by: (<b>a</b>) the weight; (<b>b</b>) a mobile crane; (<b>c</b>) a tugboat; (<b>d</b>) a vessel; and (<b>e</b>) a movable gantry crane.</p>
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<p>Filed investigation of the wharves using the IVT method.</p>
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<p>Examples of measurement data for Gemarlink wharf.</p>
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<p>The horizontal natural frequencies for: (<b>a</b>) Tan Vu wharf; (<b>b</b>) Lach Huyen Port wharf; (<b>c</b>) Hiep Phuoc wharf; and (<b>d</b>) Gemarlink wharf.</p>
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<p>The horizontal natural frequencies for: (<b>a</b>) Tan Vu wharf; (<b>b</b>) Lach Huyen Port wharf; (<b>c</b>) Hiep Phuoc wharf; and (<b>d</b>) Gemarlink wharf.</p>
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<p>Numerical simulation of a wharf.</p>
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<p>An example of IVT models with assumptions: (<b>a</b>) without erosion and (<b>b</b>) with erosion.</p>
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17 pages, 6229 KiB  
Article
Prediction of Pier Scour Depth under Extreme Typhoon Storm Tide
by Zongyu Li, Weiwei Lin, Dongdong Chu, Feng Liu, Zhilin Sun, Wankang Yang, Hanming Huang and Dan Xu
J. Mar. Sci. Eng. 2024, 12(8), 1244; https://doi.org/10.3390/jmse12081244 - 23 Jul 2024
Viewed by 821
Abstract
The Western Pacific region is highly vulnerable to typhoon storm surge disasters, with localized erosion posing a particularly prominent issue for coastal marine structures. The prevalence of extreme typhoon storm surges poses a significant threat to the safety of engineering projects in these [...] Read more.
The Western Pacific region is highly vulnerable to typhoon storm surge disasters, with localized erosion posing a particularly prominent issue for coastal marine structures. The prevalence of extreme typhoon storm surges poses a significant threat to the safety of engineering projects in these areas. In this study, a parameterized wind field model with precise calculation of wind speed was employed to establish a numerical model for typhoon storm tides. Based on the Western Pacific typhoon data from 1949 to 2023, hydraulic simulations were conducted for Hangzhou Bay, Xiangshan Port, and Yueqing Bay, revealing maximum flow velocities of 4.5 m/s, 1.95 m/s, and 2.09 m/s, respectively. These velocities exceeded the maximum possible tidal flow by 0.47–1.17 m/s. Additionally, using Sun’s velocity formula, the initiation flow velocities were calculated to be 1.85 m/s, 1.81 m/s, and 2.06 m/s for the aforementioned locations. Through localized erosion tests conducted around typical bridge piers and the subsequent application of similarity criteria, the maximum depth of localized erosion in the study area was determined to range from 2.16 m to 16.1 m, which corresponds to 1.1–2.3 times the scour caused by the maximum tidal flow scenario. A comparison of the erosion test results with calculations based on several formulas demonstrated that the scour prediction formula proposed by Sun exhibited the highest accuracy. This study supplements the understanding of the impact of typhoon storm surges on bridge pier erosion and provides a scientific basis for the design of bridge foundations. Full article
(This article belongs to the Section Physical Oceanography)
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<p>Moving track of typhoon.</p>
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<p>Verification of storm water level for the present.</p>
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<p>Experimental setup and the test section.</p>
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<p>Schematic of the experimental flume.</p>
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<p>Dimension of the experimental flume.</p>
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<p>Photo of experimental scour in the flume.</p>
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<p>Statistics of typhoons in the Western Pacific from 1949 to 2023.</p>
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<p>(<b>a</b>) Typhoons within S1 center circle; (<b>b</b>) typhoons within S2 center circle; (<b>c</b>) typhoons within S3 center circle.</p>
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<p>(<b>a</b>) Typhoons within S1 center circle; (<b>b</b>) typhoons within S2 center circle; (<b>c</b>) typhoons within S3 center circle.</p>
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<p>(<b>a</b>) Typhoons in radius of 90 km; (<b>b</b>) typhoons in radius of 180 km.</p>
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<p>(<b>a</b>) Spatial distribution of the minimum central pressure; (<b>b</b>) spatial distribution of the maximum wind speed.</p>
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<p>Comparison between 65-2 formula calculations and measured values.</p>
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<p>Comparison between Code formula calculations and measured values.</p>
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<p>Comparison between Han’s formula calculations and measured values.</p>
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<p>Comparison between Sun’s formula calculations and measured values.</p>
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21 pages, 16978 KiB  
Article
Application of New Polymer Soil Amendment in Ecological Restoration of High-Steep Rocky Slope in Seasonally Frozen Soil Areas
by Zengkang Lu, Chenglong Yu, Huanan Liu, Jiquan Zhang, Yichen Zhang, Jie Wang and Yancheng Chen
Polymers 2024, 16(13), 1821; https://doi.org/10.3390/polym16131821 - 27 Jun 2024
Cited by 1 | Viewed by 1375
Abstract
In seasonally frozen soil areas, high-steep rocky slopes resulting from open-pit mining and slope cutting during road construction undergo slow natural restoration, making ecological restoration generally challenging. In order to improve the problems of external soil attachment and long-term vegetation growth in the [...] Read more.
In seasonally frozen soil areas, high-steep rocky slopes resulting from open-pit mining and slope cutting during road construction undergo slow natural restoration, making ecological restoration generally challenging. In order to improve the problems of external soil attachment and long-term vegetation growth in the ecological restoration of high-steep rocky slopes in seasonally frozen areas, this study conducted a series of experiments through the combined application of polyacrylamide (PAM) and carboxymethyl cellulose (CMC) to assess the effects of soil amendments on soil shear strength, water stability, freeze–thaw resistance, erosion resistance, and vegetation growth. This study showed that the addition of PAM-CMC significantly increased the shear resistance and cohesion of the soil, as well as improving the water stability, freeze–thaw resistance, and erosion resistance, but the internal friction angle of the soil was not significantly increased after reaching a certain content. Moderate amounts of PAM-CMC can extend the survival of vegetation, but overuse may cause soil hardening and inhibit vegetation growth by limiting air permeability. It was observed by a scanning electron microscope (SEM) that the gel membrane formed by PAM-CMC helped to “bridge” and bind the soil particles. After discussion and analysis, the optimum application rate of PAM-CMC was 3%, which not only improved the soil structure but also ensured the growth of vegetation in the later stage under the optimum application rate. Field application studies have shown that 3% PAM-CMC-amended soil stably attaches to high-steep rocky slopes, with stable vegetation growth, and continues to grow after five months of freeze–thaw action, with no need for manual maintenance after one year. Full article
(This article belongs to the Special Issue Feature Papers in Polymer Applications II)
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<p>Soil sample collection site.</p>
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<p>Compaction curves and particle size distribution.</p>
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<p>Photographs of CMC and PAM powders and solutions.</p>
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<p>Schematic diagram of the laboratory test project.</p>
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<p>Shear strength (<b>a</b>), cohesion, and internal friction angle (<b>b</b>) for different PAM-CMC contents.</p>
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<p>Variation in disintegration ratio and disintegration rate of the specimens with time: disintegration ratio (<b>a</b>) and disintegration rate (<b>b</b>) for 3 days of curing; disintegration ratio (<b>c</b>) and disintegration rate (<b>d</b>) for 7 days of curing.</p>
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<p>Images of unamended soil and amended soil with 4% PAM-CMC.</p>
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<p>Mean frost heave rate and mean thaw settlement coefficient for different PAM-CMC contents.</p>
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<p>Images of erosion process of specimens with different PAM-CMC contents.</p>
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<p>Percentages of erosion rates for specimens with different PAM-CMC contents.</p>
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<p>Plant growth of specimens with different PAM-CMC contents.</p>
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<p>Measurements of average height of plant growth (cm).</p>
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<p>SEM images of unamended soil and 4% PAM-CMC-amended soil.</p>
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<p>Vegetation growth after spray seeding.</p>
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21 pages, 52503 KiB  
Article
Study on the Identification, Failure Mode, and Spatial Distribution of Bank Collapses after the Initial Impoundment in the Head Section of Baihetan Reservoir in Jinsha River, China
by Chuangchuang Yao, Lingjing Li, Xin Yao, Renjiang Li, Kaiyu Ren, Shu Jiang, Ximing Chen and Li Ma
Remote Sens. 2024, 16(12), 2253; https://doi.org/10.3390/rs16122253 - 20 Jun 2024
Cited by 1 | Viewed by 1094
Abstract
After the initial impoundment of the Baihetan Reservoir in April 2021, the water level in front of the dam rose about 200 m. The mechanical properties and effects of the bank slopes in the reservoir area changed significantly, resulting in many bank collapses. [...] Read more.
After the initial impoundment of the Baihetan Reservoir in April 2021, the water level in front of the dam rose about 200 m. The mechanical properties and effects of the bank slopes in the reservoir area changed significantly, resulting in many bank collapses. This study systematically analyzed the bank slope of the head section of the reservoir, spanning 30 km from the dam to Baihetan Bridge, through a comprehensive investigation conducted after the initial impoundment. The analysis utilized UAV flights and ground surveys to interpret the bank slope’s distribution characteristics and failure patterns. A total of 276 bank collapses were recorded, with a geohazard development density of 4.6/km. The slope gradient of 26% of the collapsed banks experienced an increase ranging from 5 to 20° after impoundment, whereas the remaining sites’ inclines remained unchanged. According to the combination of lithology and movement mode, the bank failure mode is divided into six types, which are the surface erosion type, surface collapse type, surface slide type, bedding slip type of clastic rock, toppling type of clastic rock, and cavity corrosion type of carbonate rock. It was found that the collapsed banks in the reservoir area of 85% developed in the reactivation of old landslide deposits, while 15% in the clastic and carbonate rock. This study offers guidance for the next phase of bank collapse regulations and future geohazards prevention strategies in the Baihetan Reservoir area. Full article
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<p>(<b>a</b>,<b>b</b>) The location of study area. (<b>c</b>) Precipitation and water level fluctuations map.</p>
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<p>Geological map of the study area.</p>
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<p>Structural map of bank slopes in the study area: (<b>a</b>) Cataclinal slope and anaclinal slope. (<b>b</b>) Orthoclinal slope. (<b>c</b>) The bank slope structure of the study area. (<b>d</b>) Cataclinal slope. (<b>e</b>) Orthoclinal slope. (<b>f</b>) Anaclinal slope.</p>
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<p>The head section of the bank collapse interpretation: (<b>a</b>) Distribution diagram of bank collapse in the study area. (<b>b</b>) Surface erosion type. (<b>c</b>) Toppling type. (<b>d</b>) Surface slide type. (<b>e</b>) Surface collapse type. (<b>f</b>) Cavity corrosion type. (<b>g</b>) Bedding slip type bank.</p>
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<p>Surface erosion type bank collapse failure model: (<b>a</b>) Field survey diagram. (<b>b</b>) Sectional diagram.</p>
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<p>Surface collapse type bank collapse failure model: (<b>a</b>) Field survey diagram. (<b>b</b>) Sectional diagram.</p>
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<p>Surface slide type bank collapse failure model: (<b>a</b>) Field survey diagram. (<b>b</b>) Sectional diagram.</p>
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<p>Bedding slide type bank collapse failure model: (<b>a</b>) Field survey diagram. (<b>b</b>) Sectional diagram.</p>
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<p>Toppling type bank collapse failure model: (<b>a</b>) Field survey diagram. (<b>b</b>) Sectional diagram.</p>
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<p>Toppling type bank collapse failure model: (<b>a</b>) Field survey diagram. (<b>b</b>) Sectional diagram.</p>
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<p>Statistical diagram of bank collapse: (<b>a</b>) Location. (<b>b</b>) Lithological group. (<b>c</b>) Bank collapse type. (<b>d</b>) Area. (<b>e</b>) Slope gradient. (<b>f</b>) Bank slope structure.</p>
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<p>Statistics of bank collapse geometric parameters: (<b>a</b>) Schematic diagram of bank collapse geometric parameters. (<b>b</b>,<b>c</b>) Statistical diagram of bank collapse geometric parameters.</p>
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<p>Photos of five sites with threats to roads, tunnels and settlements along the river. (<b>a</b>–<b>c</b>) The bank collapse threatens roads and tunnels. (<b>d</b>) Cracks in highway. (<b>e</b>) The bank collapse threatens the storeroom. (<b>f</b>) Cracks around the storeroom. (<b>g</b>,<b>h</b>) The bank collapse threatens Bridges and residential buildings.</p>
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