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Search Results (675)

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Keywords = surface settlement

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27 pages, 6813 KiB  
Article
Application of Unprocessed Waste Tyres in Pavement Base Structures: A Study on Deformation and Stress Analysis Using Finite Element Simulation
by Baoying Shen, Hui Tian, Wenruo Fan, Lu Zhang and Hui Wang
Materials 2025, 18(4), 914; https://doi.org/10.3390/ma18040914 - 19 Feb 2025
Abstract
In this study, numerical simulations using the Abaqus finite element model were performed to evaluate the effects of incorporating waste tyres of varying sizes into the base layer as part of a coupled tyre–pavement structure. The tyre-reinforced structure demonstrated superior deformation resilience, attributed [...] Read more.
In this study, numerical simulations using the Abaqus finite element model were performed to evaluate the effects of incorporating waste tyres of varying sizes into the base layer as part of a coupled tyre–pavement structure. The tyre-reinforced structure demonstrated superior deformation resilience, attributed to the hyperelastic properties of tyre rubber, underscoring its potential for applications where deformation recovery is essential. For achieving a uniform settlement, the entire tyre stacking scheme is recommended, whereas the one-third tyre configuration is ideal for minimising displacement. The one-half tyre configuration provides a balanced approach, optimising resource utilisation for structures with moderate performance requirements. The inclusion of tyres increases the equivalent stress within the cement-stabilised gravel layer beneath the tyre, and this effect is less pronounced with smaller tyre sizes. Notably, the projected portion of the tyre tread enhances the bearing capacity of the base structure, improving the load distribution and overall structural performance. The middle and bottom surface layers were identified as the most critical for controlling deformation and stress distribution, while a moderate modulus is advised for the surface course to achieve a balance between deformation control and stress uniformity. The integration of high-modulus layers with tyre reinforcement offers an optimised solution for both deformation management and stress distribution. This study highlights the potential of tyre-reinforced pavements as an innovative and sustainable construction practice, particularly suited for light to moderate traffic conditions. Further research is recommended to explore the long-term environmental and economic benefits, as well as the impacts of tyre composition and ageing on performance. Full article
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<p>A 3D model of the pavement structure.</p>
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<p>Tyre modelling. (<b>a</b>) Planar parameters; (<b>b</b>) 3D modelling.</p>
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<p>Tyre arrangement method. (<b>a</b>) Whole; (<b>b</b>) half; (<b>c</b>) one-third (third); (<b>d</b>) one-quarter (quarter).</p>
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<p>Conversion of tyre–road contact shape and equivalent area.</p>
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<p>Grid division schematic diagram. (<b>a</b>) Road grid division; (<b>b</b>) tyre grid division.</p>
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<p>Typical pavement structure deformation maps. (<b>a</b>) Original road; (<b>b</b>) one whole tyre placed; (<b>c</b>) one 1/4 tyre placed; (<b>d</b>) three whole tyres placed.</p>
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<p>Displacement results of asphalt mixture layer bottom. (<b>a</b>) One tyre placed; (<b>b</b>) three tyres placed.</p>
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<p>Displacement results of asphalt mixture layer bottom. (<b>a</b>) One tyre placed; (<b>b</b>) three tyres placed.</p>
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<p>Stress cloud of some pavement structures. (<b>a</b>) Only road (OnlyR); (<b>b</b>) one whole tyre placed; (<b>c</b>) one 1/4 tyre placed; (<b>d</b>) three whole tyres placed.</p>
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<p>Stress cloud of some pavement structures. (<b>a</b>) Only road (OnlyR); (<b>b</b>) one whole tyre placed; (<b>c</b>) one 1/4 tyre placed; (<b>d</b>) three whole tyres placed.</p>
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<p>Equivalent force variation curves in the depth direction. (<b>a</b>) One tyre placed; (<b>b</b>) three tyres placed. Note: arrow positions represent the location of structural layer changes.</p>
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<p>Equivalent force variation curves in the depth direction. (<b>a</b>) One tyre placed; (<b>b</b>) three tyres placed. Note: arrow positions represent the location of structural layer changes.</p>
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<p>Equivalent stress distribution results for Static Loads. (<b>a</b>) Top; (<b>b</b>) middle; (<b>c</b>) bottom.</p>
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<p>Equivalent stress distribution results for Static Loads. (<b>a</b>) Top; (<b>b</b>) middle; (<b>c</b>) bottom.</p>
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<p>Schematic of data observation positions.</p>
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<p>Displacement results of the top surface of the road.</p>
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<p>Equivalent stress distribution results for Moving Loads. (<b>a</b>) Top; (<b>b</b>) middle; (<b>c</b>) bottom.</p>
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<p>Equivalent stress distribution results for Moving Loads. (<b>a</b>) Top; (<b>b</b>) middle; (<b>c</b>) bottom.</p>
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<p>Impact of factors on MDBSL.</p>
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<p>Impact of factors on EDESDD.</p>
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18 pages, 7632 KiB  
Article
Research on the Fine Control of the Influence of Pipe-Jacking Parameter Deviation on Surrounding Stratum Deformation
by Tianlong Zhang, Guoqing Chen, Ping Lu and Dongqing Nie
Appl. Sci. 2025, 15(4), 2208; https://doi.org/10.3390/app15042208 - 19 Feb 2025
Abstract
Based on the Zhuyuan–Bailonggang sewage interconnection pipe project in Shanghai, the ABAQUS finite element software was used in numerical simulations to study the fine control of stratum disturbances caused by pipe jacking parameter deviation in soft soil areas. Combining the simulation results with [...] Read more.
Based on the Zhuyuan–Bailonggang sewage interconnection pipe project in Shanghai, the ABAQUS finite element software was used in numerical simulations to study the fine control of stratum disturbances caused by pipe jacking parameter deviation in soft soil areas. Combining the simulation results with onsite measured data, the Peck formula was used to predict surface settlement. The results indicate the following: (1) The jacking speed and face pressure are negatively correlated with surface settlement. Under the maximum positive deviation and negative deviations in the jacking speed, after the tail passes through the monitoring section D0 16 ring, the maximum value of settlement at point B8 increases by 21.6% and decreases by 12.8%, respectively. Increasing the jacking speed increases the area with stress change ratio R < 0 at monitoring section D0, and the arch foot at the tail of the pipe jacking machine decreases the surface settlement. In contrast, when the face pressure deviates from its average value, the variation range is less than 1%. (2) The pipe slurry coefficient and surface subsidence are positively correlated. Under the maximum positive deviation and the maximum negative deviation, the tail passes through the monitoring section D0 16 ring, and the maximum settlement value at B8 decreases by 4.9% and increases by 16.5%, respectively. The increase in the coefficient reduces the area with R < 0 at D0 and increases the surface settlement. (3) In the order of descending strength, surface settlement is affected by the jacking speed, slurry friction coefficient, and face pressure. (4) To predict the maximum surface settlement value due to deviations in the jacking parameters, the Peck formula was modified using a correction factor α ranging from 0.6 to 3.0 and a settlement trough width correction factor β ranging from 1.6 to 4.0. The modified prediction curve is in closer agreement with the actual conditions. Full article
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<p>Plane layout of monitoring points.</p>
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<p>Surface subsidence monitoring curves: (<b>a</b>) lateral settlement; (<b>b</b>) longitudinal settlement.</p>
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<p>Jacking parameter fluctuation diagram.</p>
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<p>Finite element model and size.</p>
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<p>Calculated curve and measured results of ground settlement at D<sub>0</sub>.</p>
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<p>Influence of the jacking speed deviation on the ground settlement.</p>
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<p>Change in the transverse settlement tank under different jacking speeds.</p>
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<p>Comparison diagram of the vertical stress on the soil arch under two kinds of jacking speeds: (<b>a</b>) <math display="inline"><semantics> <mi>v</mi> </semantics></math> = 2 ring/d; (<b>b</b>) <math display="inline"><semantics> <mi>v</mi> </semantics></math> = 10 ring/d.</p>
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<p>Influence of tunnel face pressure deviation on ground settlement.</p>
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<p>Comparison diagram of the vertical stress on the soil arch under two kinds of tunnel face pressures: (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mi>p</mi> <mi>N</mi> </msub> <mo>=</mo> <mn>100</mn> <mi>kPa</mi> </mrow> </semantics></math>; (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mi>p</mi> <mi>N</mi> </msub> <mo>=</mo> <mn>140</mn> <mi>kPa</mi> </mrow> </semantics></math>.</p>
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<p>Influence of the friction coefficient deviation on ground settlement.</p>
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<p>Change diagram of the transverse settlement tank under different coefficients of friction.</p>
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<p>Comparison diagram of the vertical stress on the soil arch under two coefficients of friction: (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>μ</mi> <mo>=</mo> <mn>0.01</mn> </mrow> </semantics></math>; (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>μ</mi> <mo>=</mo> <mn>0.09</mn> </mrow> </semantics></math>.</p>
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<p>Normalized vertical surface displacement caused by parameter deviation.</p>
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<p>Peck fitting, prediction, and comparison of the measured data curves.</p>
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<p>Peck prediction correction, fitting, and comparison of measured data curves.</p>
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<p>Distribution intervals of the α and β data: (<b>a</b>) <math display="inline"><semantics> <mi>α</mi> </semantics></math> data distribution diagram; (<b>b</b>) <math display="inline"><semantics> <mi>β</mi> </semantics></math> data distribution diagram.</p>
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<p>Comparison of the corrected Peck upper and lower limit curves with the measured data.</p>
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20 pages, 7217 KiB  
Article
The Field Monitoring and Numerical Simulation of Spatiotemporal Effects During Deep Excavation in Mucky Soft Soil: A Case Study
by Qiang Wu, Jianxiu Wang, Yanxia Long, Xuezeng Liu, Guanhong Long, Shuang Ding, Li Zhou, Huboqiang Li and Muhammad Akmal Hakim bin Hishammuddin
Appl. Sci. 2025, 15(4), 1992; https://doi.org/10.3390/app15041992 - 14 Feb 2025
Abstract
The issue of geotechnical hazards induced by excavation in soft soil areas has become increasingly prominent. However, the retaining structure and surface settlement deformation induced by the creep of soft soil and spatial effect of the excavation sequence are not fully considered where [...] Read more.
The issue of geotechnical hazards induced by excavation in soft soil areas has become increasingly prominent. However, the retaining structure and surface settlement deformation induced by the creep of soft soil and spatial effect of the excavation sequence are not fully considered where only elastic–plastic deformation is used in design. To understand the spatiotemporal effects of excavation-induced deformation in soft soil pits, a case study was performed with the Huaxi Park Station of the Suzhou Metro Line S1, Jiangsu Province, China, as an example. Field monitoring was conducted, and a three-dimensional numerical model was developed, taking into account the creep characteristics of mucky clay and spatiotemporal response of retaining structures induced by excavations. The spatiotemporal effects in retaining structures and ground settlement during excavation processes were analyzed. The results show that as the excavation depth increased, the horizontal displacement of the diaphragm walls increased linearly and tended to exhibit abrupt changes when approaching the bottom of the pit. The maximum horizontal displacement of the wall at the west end well was close to 70 mm, and the maximum displacement of the wall at the standard section reached approximately 80 mm. The ground settlement on both pit sides showed a “trough” distribution pattern, peaking at about 12 m from the pit edge, with a settlement rate of −1.9 mm/m per meter of excavation depth. The excavation process directly led to the lateral deformation of the diaphragm walls, resulting in ground settlement, which prominently reflected the time-dependent deformation characteristics of mucky soft soil during the excavation process. These findings provide critical insights for similar deep excavation projects in mucky soft soil, particularly regarding excavation-induced deformations, by providing guidance on design standards and monitoring strategies for similar geological conditions. Full article
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<p>Soil profile along the standard section of Huaxi Park Station.</p>
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<p>Layout of monitoring points of Huaxi Park Station foundation pit. (CX is the monitoring point number of diaphragm wall horizontal displacement; DB is the monitoring point number of surface subsidence).</p>
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<p>A 3D numerical model of the Huaxi Park Station foundation pit.</p>
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<p>Structure of CVISC model.</p>
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<p>Variation rule of maximum horizontal displacement of enclosure wall: (<b>a</b>) maximum horizontal displacement of west end well wall; (<b>b</b>) maximum horizontal displacement of standard section wall. RW means retaining wall.</p>
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<p>Surface settlement outside the pit: (<b>a</b>) surface settlement outside the west end head pit; (<b>b</b>) surface settlement outside the standard section pit. D is the distance from the pit. Notes−excavation step sequence: 1−arrangement of the first steel support; 2−arrangement of the second steel support; 3−arrangement of the third steel support; 4−arrangement of the fourth steel support; 5−excavation completed.</p>
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<p>The relationship between the surface settlement outside the pit and the maximum horizontal displacement of the retaining wall: (<b>a</b>) the west end well; (<b>b</b>) the standard section.</p>
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<p>Pore water pressure contour with different construction steps: (<b>a</b>) before excavation; (<b>b</b>) excavation of third floors; (<b>c</b>) final excavation.</p>
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<p>Pore water pressure contour with different construction steps: (<b>a</b>) before excavation; (<b>b</b>) excavation of third floors; (<b>c</b>) final excavation.</p>
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<p>Horizontal displacement of diaphragm wall of Huaxi Park Station foundation pit.</p>
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<p>Horizontal displacement of diaphragm wall (CX5): (<b>a</b>) horizontal displacement versus depth curve; (<b>b</b>) variation curve of maximum horizontal displacement with construction sequence. (Construction sequence: 1—arrangement of the first steel support; 2—arrangement of the second steel support; 3—arrangement of the third steel support; 4—arrangement of the fourth steel support; 5—arrangement of the fifth steel support; 6—completion of the footing pouring.)</p>
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<p>Vertical displacement after the completion of excavation: (<b>a</b>) surface settlement outside the pit; (<b>b</b>) vertical displacement.</p>
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<p>Surface settlement outside the pit after the completion of excavation: (<b>a</b>) DB4; (<b>b</b>) DB6; (<b>c</b>) DB1.</p>
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<p>Change in the axial force of the first concrete support.</p>
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<p>Change in the axial force of the second to fifth supports.</p>
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26 pages, 8047 KiB  
Article
A Case Study on Fuzzy Analytic Hierarchy Process Analysis of Factors Influencing the Stability of Surrounding Rock in Water-Rich Loess Tunnels and Corresponding Disposal Strategies
by Xin Ren, Tianhu He, Pengfei He, Feng Yue and Bo Yang
Appl. Sci. 2025, 15(4), 1835; https://doi.org/10.3390/app15041835 - 11 Feb 2025
Abstract
Tunnel excavation in water-rich and saturated loess layers often encounters a series of engineering disasters, including surface settlement, large deformations of surrounding rock, collapses, water inrushes, mud inrushes, and lining cracks. This paper presents an analogy of 16 cases of instability and collapse [...] Read more.
Tunnel excavation in water-rich and saturated loess layers often encounters a series of engineering disasters, including surface settlement, large deformations of surrounding rock, collapses, water inrushes, mud inrushes, and lining cracks. This paper presents an analogy of 16 cases of instability and collapse of surrounding rock during the excavation of water-rich loess tunnels in China’s loess regions. The weight of influence of various factors affecting the stability of surrounding rocks has been analyzed based on the Fuzzy Analytic Hierarchy Process (FAHP), addressing the engineering challenges encountered during the construction of the Tuanjie Tunnel. Measures such as deep well-point dewatering of the surface, reinforcement of locking foot anchors, and construction treatment with large arch feet are proposed. The effectiveness of these treatments is then monitored and analyzed. The results show that after 30 days of dewatering, the average water content of the surrounding rock decreased from 28.8% to 22.3%, transforming the surrounding rock from a soft plastic state to a hard plastic state. Phenomena such as mud inrushes at the tunnel face and water seepage through the lining are significantly reduced, and the self-stabilizing capacity of the surrounding rock is markedly improved. By optimizing the excavation method and enhancing support parameters, the construction progress rate for Grade VI surrounding rock has increased from 10–15 m per month to 40 m per month, validating the effectiveness of the proposed measures. Full article
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<p>Schematic diagram of the location of Tuanjie Tunnel.</p>
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<p>Geological profile of the left entrance of the Tuanjie Tunnel.</p>
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<p>A series of engineering disasters encountered during the construction of the Tuanjie Tunnel.</p>
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<p>The comprehensive response measures.</p>
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<p>A schematic diagram of the construction method transition in the experimental section.</p>
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<p>Schematic diagram of sensor layout types for each measuring point on the monitoring section.</p>
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<p>The on-site installation images of the sensors.</p>
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<p>The variation curve of moisture content at measuring points with monitoring time and excavation space.</p>
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<p>Distribution pattern of rock moisture content around the cave before and after precipitation (red lines indicate before precipitation, green lines indicate after precipitation).</p>
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<p>Radial cumulative displacement distribution inside the rock surrounding the cave (unit: mm).</p>
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<p>Time–history curve of arch settlement and horizontal convergence deformation around the tunnel.</p>
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<p>Time history curve of contact pressure changes between the surrounding rock and the initial support in the monitoring section.</p>
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<p>Schematic diagram of contact pressure distribution between surrounding rock and initial support in the monitoring section.</p>
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<p>Stacked bar chart of percentage of contact pressure between surrounding rock and initial support at different stages of each measuring point.</p>
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14 pages, 3922 KiB  
Article
Experimental Study on the Symmetry of the Soil-Arching Effect of a Pile Foundation in a Reinforced High-Fill Area
by Liangdong Zuo, Quanbao Wang and Jia Liu
Symmetry 2025, 17(2), 188; https://doi.org/10.3390/sym17020188 - 25 Jan 2025
Viewed by 228
Abstract
In addition to the vertical external load and soil settlement load, the pile foundation in reinforced high-fill areas is also affected by the horizontal load caused by the rear stacking load, and pile stress is affected by the soil-arching effect in reinforced areas [...] Read more.
In addition to the vertical external load and soil settlement load, the pile foundation in reinforced high-fill areas is also affected by the horizontal load caused by the rear stacking load, and pile stress is affected by the soil-arching effect in reinforced areas that have typical passive pile characteristics. In order to study the symmetry of the soil-arching effect of pile foundations in a reinforced-fill area, indoor model tests were designed and the relevant data for the pile foundation and reinforced soil under surcharge were obtained. Through the analysis, the following conclusions were drawn: the peak bending moment of the pile body is basically consistent with the position of the potential sliding surface of reinforced soil; the maximum shear force of the pile body appears about 150 mm below the embedding point; with an increase in depth, the soil-arching effect becomes obvious. There are two different forms of friction, soil-arching and direct soil-arching between piles and behind piles, and the soil between single-row piles has a symmetrical distribution. In addition to the vertical external load and soil settlement load, the pile foundation in reinforced high-fill areas will also be affected by the horizontal load caused by the rear stacking load, and pile stress will be affected by the soil-arching effect in reinforced areas, which has typical passive pile characteristics. In order to study the symmetry of the soil-arching effect of pile foundations in a reinforced-fill area, indoor model tests were designed, and the relevant data for pile foundation and reinforced soil under surcharge were obtained. Through analysis, the following conclusions were drawn: (1) the peak bending moment of the pile body is basically consistent with the position of the potential sliding surface of reinforced soil; the maximum shear force of the pile body appears about 150 mm below the embedding point; with an increase in depth, the soil-arching effect becomes obvious. There are two different forms of friction, soil-arching and direct soil-arching between piles and behind piles, and the soil between single-row piles has a symmetrical distribution. Full article
(This article belongs to the Section Engineering and Materials)
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<p>Model test design (unit: mm).</p>
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<p>Test pool and model pile.</p>
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<p>Strain gauge arrangement of the model pile.</p>
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<p>Design and manufacturing of model ribbon.</p>
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<p>Filling process of the reinforced soil model.</p>
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<p>Loading and monitoring design.</p>
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<p>Loading and monitoring process.</p>
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<p>Monitoring results of the pile-bending moment.</p>
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<p>Monitoring results of pile shearing force.</p>
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<p>Distribution of earth pressure behind piles.</p>
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15 pages, 33004 KiB  
Article
The Characterization of the Lower Town of the UNESCO Archaeological Site of Arslantepe (Malatya, Türkiye) Using the Geophysical E-PERTI Method (Extended Data-Adaptive Probability-Based Electrical Resistivity Tomography Inversion Method)
by Francesca Balossi Restelli, Marilena Cozzolino, Federico Manuelli and Paolo Mauriello
Heritage 2025, 8(2), 37; https://doi.org/10.3390/heritage8020037 - 22 Jan 2025
Viewed by 389
Abstract
The UNESCO site of Arslantepe is located in Eastern Anatolia in the Malatya Plain (Türkiye) about 10 km from the Euphrates River. Here for about a century archaeological excavations have been carried out, reconstructing a long sequence of human frequentation starting from 5000 [...] Read more.
The UNESCO site of Arslantepe is located in Eastern Anatolia in the Malatya Plain (Türkiye) about 10 km from the Euphrates River. Here for about a century archaeological excavations have been carried out, reconstructing a long sequence of human frequentation starting from 5000 years BC up to the Middle Ages. The settlement, one of the most important and largest in the region, has undergone numerous changes over time, resulting in a complex superposition of structures, palaces, temples, and burials concentrated on the hill. With the aim of extending the knowledge of the site, in 2022, geophysical surveys were carried out through the application of electrical resistivity tomography, covering a surface of approximately 4300 m2 in an unexplored area at the foot of the hill. In this paper, the Extended data-adaptive Probability-based Electrical Resistivity Tomography Inversion approach (E-PERTI), recently published as a development of the probability tomography imaging approach, has been applied to a large apparent resistivity field dataset, providing the best estimate of the most probable estimate of the resistivity distribution through an intrinsic linear regression model implementing standard least squares routines. The results seem to prove the effectiveness of the E-PERTI approach in noise dejection, enhancing associated resistivity highs that can be ascribable to the trace of a potential fortification. The obtained information represents new, unexpected data that open new frontiers of archaeological research, adding value to the knowledge of the site. Full article
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<p>Position of Arslantepe on a physical map of Türkiye and the eastern Mediterranean basin and location of the survey area on an aerial view of the hill.</p>
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<p>The ERT survey planning at the northern foot of the hill of Arslantepe (<b>a</b>), and data acquisition with MAE A3000<sup>TM</sup> resistivity meter along Line 9 (<b>b</b>).</p>
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<p>L10 (<b>a</b>) and L31 (<b>b</b>) profiles: apparent resistivity pseudosection and the extraction of the Nq tests in depth are reported (from top to bottom k = 2, k = 3, k = 4, k = 5).</p>
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<p>L42 (<b>a</b>) and L20 (<b>b</b>) profiles: apparent resistivity pseudosection and the extraction of the Nq tests in depth are reported (from top to bottom k = 2, k = 3, k = 4, k = 5).</p>
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<p>L10 (<b>a</b>) and L40 (<b>b</b>) profiles: comparison between E-PERTI and ZondRes2D inversion.</p>
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<p>Sequence of horizontal slices at increasing depth of 1.5 m (<b>a</b>), 2.25 m (<b>b</b>), 3.0 m (<b>c</b>), and 3.75 m (<b>d</b>) beneath the ground level overlapped to a satellite image. A and B mark the two high-resistivity volumes.</p>
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<p>Three-dimensional ERT model obtained by the assemblage of the E-PERTI sections (<b>a</b>,<b>b</b>) showing also some vertical (<b>c</b>,<b>d</b>) and horizontal slices (<b>e</b>,<b>f</b>). The A and B letters are used to highlight the location of the high-resistivity bodies.</p>
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<p>Overlapping of geophysical results on the archaeological map relative to the Early Iron Age (<b>a</b>) and on an aerial picture (<b>b</b>). The fortification is marked with magenta arrows and the gates with blue arrows, both those known and those hypothesized (signed with “?"). The A and B letters are used to highlight the location of the high-resistivity bodies (compare with <a href="#heritage-08-00037-f006" class="html-fig">Figure 6</a> and <a href="#heritage-08-00037-f007" class="html-fig">Figure 7</a>).</p>
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<p>Interpretive sketch of the discovered resistivity structure.</p>
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15 pages, 941 KiB  
Article
Sidewall Roughness Measurement and Bearing Performance Simulation of Rock-Socketed Piles Based on Laser Scanning Point Cloud
by Junbao Zhang, Yule Hu, Yiteng Wang and Di Zhang
Appl. Sci. 2025, 15(2), 889; https://doi.org/10.3390/app15020889 - 17 Jan 2025
Viewed by 335
Abstract
Rock-socketed piles are commonly used in pile foundations for large buildings because of their excellent load-bearing characteristics. The roughness of the pile–rock interface affects the load transfer and the ultimate side resistance of the pile. In this work, a laser radar system is [...] Read more.
Rock-socketed piles are commonly used in pile foundations for large buildings because of their excellent load-bearing characteristics. The roughness of the pile–rock interface affects the load transfer and the ultimate side resistance of the pile. In this work, a laser radar system is developed to measure the surface roughness of a dry bored pile and the shape of the borehole, and a three-dimensional model of the borehole is reconstructed based on the laser point cloud. The 3D surface model was used to extract the vertical contour lines in different directions and thus calculate the roughness of the pile. A numerical simulation of the real measured 3D model using FLAC3D is presented. A borehole of a real rock-socketed pile was measured and simulated. The results show that, although the working load is carried by both the side and base resistances, the former plays a major role. The slow-varying load-settlement curve indicates that the pile has a superior load–bearing capacity, and the maximum allowable settlement should be considered in the application. The simulations, using the actual piles tested, produced a more realistic load response and were able to predict the load-bearing performance of the piles more accurately. Furthermore, this approach offers a reference for the design of rock-socketed piles. Full article
(This article belongs to the Section Civil Engineering)
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<p>Roughness models defined by Monash University and Horvath [<a href="#B8-applsci-15-00889" class="html-bibr">8</a>].</p>
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<p>Photographs of the LiDAR system.</p>
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<p>Schematic diagram of the laser scanning system.</p>
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<p>Extraction of contour lines from a 3D mesh model for roughness calculation.</p>
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<p>Dimensioning and boundary setting of the overall model.</p>
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<p>Reconstruction of the borehole surface model.</p>
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<p>Rough contour lines for bored piles in different directions.</p>
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<p>Slicing of the mesh model in FLAC3D.</p>
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<p>Load–displacement curves of the piles.</p>
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<p>Unit side resistance with depth for the pile under different loads.</p>
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<p>Side resistance of different pile sections at relative pile-rock displacements.</p>
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<p>Axial force distribution along the depth for the pile.</p>
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<p>Distribution of <math display="inline"><semantics> <mrow> <mi>Z</mi> <mi>Z</mi> </mrow> </semantics></math>-Stress under a load of 7 MPa.</p>
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27 pages, 6768 KiB  
Article
Complex Study of Settlements Dating from the Paleolithic to Medieval Period in the Ural Mountains on the Border of Europe and Asia
by Valentina Prikhodko, Nikita Savelev, Vyacheslav Kotov, Sergey Nikolaev, Evgeny Ruslanov, Mikhail Rumyantsev and Elena Manakhova
Geosciences 2025, 15(1), 31; https://doi.org/10.3390/geosciences15010031 - 16 Jan 2025
Viewed by 391
Abstract
Soil, geochemical, microbiological, and archeological studies were conducted at eight settlements dating from the Paleolithic to Late Medieval and Modern Ages near the southern Trans-Urals Mountains, Russia. The forest-steppe landscapes, rivers, and abundant mineral resources have attracted people to the region since ancient [...] Read more.
Soil, geochemical, microbiological, and archeological studies were conducted at eight settlements dating from the Paleolithic to Late Medieval and Modern Ages near the southern Trans-Urals Mountains, Russia. The forest-steppe landscapes, rivers, and abundant mineral resources have attracted people to the region since ancient times. Cultural layers (CLs) are marked by finds of ceramics fragments, animal bones, stone, and metal tools. The properties of CLs include close-to-neutral pH, being well structured, the absence of salinity, enrichment with exchangeable calcium, and anthropogenic phosphorus (0.2–0.4%). The majority of CLs start at a depth of 3–25 cm, extend to 40–60 cm, and contain 6–10% organic carbon (Corg) in the 0–20 cm layer, reflecting carbon input from modern-day processes. At the Ishkulovo site (0.6–0.8 ka BP), Corg decreases to 1.3% because the CL is below 80 cm, and in the absence of fresh organic material input, carbon has been mineralized. The proximity of sites to deposits of copper, chromium, zinc, and manganese in the Ural Mountains creates natural high-content anomalies in the region, as indicated by their abundance in soils and parent rocks. In the past, these elements were also released into CLs from metal products, ceramic fragments, and raw materials used in their manufacture. The sites are quite far (18–60 km) from the Magnitogorsk Metallurgical plant, but industrial stockpiles of S (technogenic coefficient—Ct 30–87%), and, less often, Cr, Mn, and Sr (Ct 30–40%) accumulated in surface layers. These three factors have led to the concentration of pollutants of the first (arsenic, chromium, lead, and zinc) and second (cobalt, copper, and nickel) hazard classes at CLs, often in quantities 2–5 times higher than values for parent materials and geosphere average content (“Clarke” value), and, and less often, more than the allowable content for human health. This may have influenced their health and behavioral functions. Due to the above properties, chernozems have a high buffering capacity and a strong bond with heavy metals. Therefore, no inhibition of microbes was observed. The microbial biomass of the 0–10 cm layer is high, 520–680 µg C/g, and microbes cause the emission of 1.0 C-CO2 µg/g of soil per hour. During the ancient settlements’ development, a favorable paleoclimate was noted based on the data cited. This contributed to the spread of productive paleolandscapes, ensuring the development of domestic cattle breeding and agriculture. Full article
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<p>Study area location: (<b>A</b>)—Baskortostan Republic in Russia, (<b>B</b>)—Abzelilovskiy district within Bashkortostan, (<b>C</b>)—locations of the sites studied in the region around Magnitogorsk (<a href="https://opentopomap.org/#map=12/53.6136/58.6776" target="_blank">https://opentopomap.org/#map=12/53.6136/58.6776</a>, accessed on 3 January 2024).</p>
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<p>(<b>A</b>) Locations of Kusimovo-8, 6, and 7 sites. Quadcopter view. Photo by A.A. Khurmaev, 2021, (<b>B</b>) landscape near the Kusimovo and Sabakty-1a; sites. (<b>C</b>) three Paleolithic stone tools in different angles from the Kusimovo-8 site.—one stone tool in different angles.</p>
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<p>Soil and CLs at the sites of (<b>A</b>) Kusimovo-8, (<b>B</b>) Ishkulovo, (<b>C</b>) Elimbetovo-7, (<b>D</b>) Sabakty-1a.</p>
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<p>The granulometry of the sites.</p>
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<p>The granulometry of the sites.</p>
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<p>pH, iron, microbial biomass, and basal respiration of the sites. * In all figures, dashed line means the Clarke value, region—regional elements content accordion (8).</p>
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<p>Content of Corg, total nitrogen, and phosphorus; C/N ratio of the sites.</p>
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<p>(<b>a</b>) Content of some microelements of the sites. (<b>b</b>) Content of some microelements of the sites. (<b>c</b>) Content of potassium and manganese at the sites. Dashed line means the Clarke value, region—regional elements content accordion (8).</p>
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<p>(<b>a</b>) Content of some microelements of the sites. (<b>b</b>) Content of some microelements of the sites. (<b>c</b>) Content of potassium and manganese at the sites. Dashed line means the Clarke value, region—regional elements content accordion (8).</p>
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<p>(<b>a</b>) Content of some microelements of the sites. (<b>b</b>) Content of some microelements of the sites. (<b>c</b>) Content of potassium and manganese at the sites. Dashed line means the Clarke value, region—regional elements content accordion (8).</p>
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22 pages, 4457 KiB  
Article
Sensitivity Analysis and Application of the Shanghai Model in Ultra-Deep Excavation Engineering
by Aoyang Ma, Weiyi Wang, Wenxuan Zhu, Zhonghua Xu and Guanlin Ye
Geotechnics 2025, 5(1), 6; https://doi.org/10.3390/geotechnics5010006 - 13 Jan 2025
Viewed by 330
Abstract
In deep foundation pit engineering, the soil undergoes a complex stress path, encompassing both loading and unloading phases. The Shanghai model, an advanced constitutive model, effectively accounts for the soil’s deformation characteristics under these varied stress paths, which is essential for accurately predicting [...] Read more.
In deep foundation pit engineering, the soil undergoes a complex stress path, encompassing both loading and unloading phases. The Shanghai model, an advanced constitutive model, effectively accounts for the soil’s deformation characteristics under these varied stress paths, which is essential for accurately predicting the horizontal displacement and surface settlement of the foundation pit’s enclosure structure. This model comprises eight material parameters, three initial state parameters, and one small-strain parameter. Despite its sophistication, there is a scarcity of numerical studies exploring the correlation between these parameters and the deformation patterns in foundation pit engineering. This paper initially establishes the superiority of the Shanghai model in ultra-deep circular vertical shaft foundation pit engineering by examining a case study of a nursery circular ultra-deep vertical shaft foundation pit, which is part of the Suzhou River section’s deep drainage and storage pipeline system pilot project in Shanghai. Subsequently, utilizing an idealized foundation pit engineering model, a comprehensive sensitivity analysis of the Shanghai model’s multi-parameter values across their full range was performed using orthogonal experiments. The findings revealed that the parameter most sensitive to the lateral displacement of the underground continuous wall was κ, with an increase in κ leading to a corresponding increase in displacement. Similarly, the parameter most sensitive to surface subsidence outside the pit was λ, with an increase in λ resulting in greater subsidence. Lastly, the parameter most sensitive to soil uplift at the bottom of the pit was also κ, with an increase in κ leading to more significant uplift. Full article
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<p>Numerical research path of deep excavation engineering based on Shanghai model.</p>
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<p>Superloading surface, normal yield surface, and subloading surface of soil.</p>
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<p>Introduction to constitutive parameters of Shanghai model.</p>
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<p>Layout of measurement points and structural parameters for deep foundation pit engineering in Miaopu.</p>
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<p>Three-dimensional finite element calculation model of Miaopu foundation pit.</p>
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<p>Finite element results of lateral displacement of underground continuous wall upon completion of foundation pit construction. (<b>a</b>) X-directional displacement of underground continuous wall (east side); (<b>b</b>) Y-direction displacement of underground continuous wall (north side); (<b>c</b>) total displacement of underground continuous wall.</p>
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<p>Comparison between the calculation results and actual measurements of the lateral displacement of the underground continuous wall at each stage.</p>
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<p>Comparison between the calculation results and actual measurements of the lateral displacement of the underground continuous wall at each stage.</p>
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<p>Finite element results of surface settlement outside the pit.</p>
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<p>Comparison between the calculated and measured settlement results of the surface soil outside the pit.</p>
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<p>Sensitivity study model of excavation engineering parameters.</p>
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<p>Orthogonal experimental research results.</p>
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21 pages, 4888 KiB  
Article
Evaluating Consolidation Behaviors in High Water Content Oil Sands Tailings Using a Centrifuge
by Mahmoud Ahmed, Nicholas A. Beier and Heather Kaminsky
Geotechnics 2025, 5(1), 3; https://doi.org/10.3390/geotechnics5010003 - 7 Jan 2025
Viewed by 650
Abstract
The composition of oil sands tailings is a complex mixture of water, fine clay, sand, silt, and residual bitumen that remains after the extraction of bitumen. Effective tailings disposal management requires an understanding of the mechanisms controlling water movement, surface settlement rates and [...] Read more.
The composition of oil sands tailings is a complex mixture of water, fine clay, sand, silt, and residual bitumen that remains after the extraction of bitumen. Effective tailings disposal management requires an understanding of the mechanisms controlling water movement, surface settlement rates and extents (hydraulic conductivity and compressibility), and strength variation with depth. This investigation examines the self-weight consolidation behavior of oil sands tailings, typically assessed by utilizing large strain consolidation (LSC) methods such as the multi-step large strain consolidation (MLSC) test and seepage-induced consolidation test (SICT). These methods, however, are time consuming and often take weeks or years to complete. As an alternative, centrifuge testing, including both geotechnical beam type and benchtop devices, was utilized to evaluate the consolidation behaviors of three untreated high water content oil sands tailing slurries: two high-plasticity fluid fine tailing (FFT) samples and one low plasticity FFT. The centrifuge-derived compressibility data closely matched the LSC testing compressibility data within the centrifuge stress range. However, the hydraulic conductivity obtained from centrifuge testing was up to an order of magnitude higher than the LSC test results. Comparing centrifuge and large strain modeling results indicates that centrifuge test data demonstrate average void ratios 10–33% lower than those predicted by simulations using LSC parameters, highlighting a notable deviation. To examine the scale effect on result accuracy, validation tests indicated that the benchtop centrifuge (BTC) yielded comparable results to the geotechnical beam centrifuge (GBC) for the same prototype, saving time, resources, and sample volumes in the assessment of tailings consolidation behavior. These tests concluded that the small radius of the benchtop centrifuge had a minimal impact on the results. Full article
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<p>The GeoCERF geotechnical centrifuge setup: (<b>a</b>) the centrifuge and its instrumentation, (<b>b</b>) the consolidation cells on the swing platform before spinning, and (<b>c</b>) the cells after spinning.</p>
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<p>Consolidation cell filled with slurry and pore water pressure transducers.</p>
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<p>(<b>a</b>) Particle size distribution of the three oil sands tailings samples and (<b>b</b>) Casagrande plasticity chart for all tailings samples.</p>
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<p>Matching the consolidation curve from FSCA numerical simulations with the curve derived from GBC modeling of the 40 m prototype. (<b>a</b>) Fitting power law function to the final void ratio-effective stress distribution. (<b>b</b>) Fitting measured GBC height with FSCA numerical simulation interface height curve.</p>
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<p>Comparison of FSCA numerical simulation consolidation curves with measured GBC modeling curves: (<b>a</b>) compressibility curves for a 40 m prototype, (<b>b</b>) matching the 40 m prototype’s numerical simulation consolidation curve with the GBC modeling curve, (<b>c</b>) compressibility curves for a smaller prototype, (<b>d</b>) matching the smaller prototype’s numerical simulation consolidation curve with the GBC modeling curve.</p>
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<p>MLSC vs. centrifuge testing compressibility results for the tested oil sands tailings: (<b>a</b>) FFT-91-10.8, (<b>b</b>) FFT-89-7.8, and (<b>c</b>) FFT-71-5.8.</p>
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<p>MLSC vs. centrifuge testing hydraulic conductivity results for the tested oil sands tailings: (<b>a</b>) FFT-91-10.8, (<b>b</b>) FFT-89-7.8, and (<b>c</b>) FFT-71-5.8.</p>
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<p>SICT vs. centrifuge testing compressibility results for the tested oil sands tailings: (<b>a</b>) FFT-91-10.8 and (<b>b</b>) FFT-89-7.8.</p>
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<p>SICT vs. centrifuge testing hydraulic conductivity results for the tested oil sands tailings: (<b>a</b>) FFT-91-10.8 and (<b>b</b>) FFT-89-7.8.</p>
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<p>Temporal variations in the average void ratio from centrifuge testing and large-strain modeling for the tested tailings, based on parameters derived from SICT: (<b>a</b>) FFT-91-10.8 and (<b>b</b>) FFT-89-7.8.</p>
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<p>Temporal variations of the normalized prototype height from centrifuge testing and large-strain modeling for the tested tailings, based on parameters derived from SICT: (<b>a</b>) FFT-91-10.8 and (<b>b</b>) FFT-89-7.8 (normalized prototype height is defined as the ratio of the prototype height to the initial prototype height).</p>
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<p>Comparison of the BTC and GBC tests: (<b>a</b>) average void ratio and (<b>b</b>) normalized prototype height.</p>
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19 pages, 4651 KiB  
Article
Evaluation of Dynamic Compaction Load Conversion Methods and Vibration Reduction Treatments
by Jixuan Li, Wenli Wang, Longping Luo, Xiaoliang Yao and Jiangang Hu
Buildings 2025, 15(1), 111; https://doi.org/10.3390/buildings15010111 - 31 Dec 2024
Viewed by 431
Abstract
This study aims to evaluate the accuracy of different dynamic compaction (DC) load equivalent conversion methods in DC vibration calculations. It also investigates the effect of vibration isolation treatments on the vibration reduction performance of loess foundations, with the goal of optimizing vibration [...] Read more.
This study aims to evaluate the accuracy of different dynamic compaction (DC) load equivalent conversion methods in DC vibration calculations. It also investigates the effect of vibration isolation treatments on the vibration reduction performance of loess foundations, with the goal of optimizing vibration control during DC construction. Five classical methods were used to convert the DC loads into time-dependent surface loads, which were subsequently fed into Plaxis’s dynamic multiplier table for the numerical implementation of DC tests. By comparing the numerical simulation results with in situ monitoring data from a loess site, the accuracy of the five DC load equivalent conversion methods was evaluated. The momentum theorem method was identified as the most precise for both vibration velocity and settlement. Subsequently, the momentum theorem method was utilized to investigate the influence of depth and distance of vibration isolation trench, as well as the properties of vibration isolation materials on vibration reduction effect. It is indicated that the optimal depth for the vibration isolation trench of the loess site is 2 m, beyond which the improvement in vibration reduction effects is not notable. The excavation distance of the vibration isolation trench should be set as close as possible to the boundary of the construction site to achieve the best vibration reduction effect. As for the properties of vibration isolation materials, it is shown that the unit weight and damping ratio of the filling material have a significant effect on the vibration reduction effect, while the influence of the shear strength of the filling material is negligible. Besides the vibrating reduction influence of filling materials, utilizing spring dampers has a better vibration reduction effect. Increasing the stiffness of the spring dampers and reducing their spacing can significantly enhance the vibration reduction effect. In practical engineering applications, it is essential to consider both the effects and economic costs to select the optimal vibration reduction treatment and its parameters. This study provides a scientific basis for vibration control during DC construction, contributing to ensuring construction safety and efficiency while minimizing the impact on the surrounding environment. Full article
(This article belongs to the Section Construction Management, and Computers & Digitization)
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<p>Schematic diagram of site vibration monitoring points: (<b>a</b>) plan view of the field test; (<b>b</b>) cutaway view of the field test.</p>
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<p>DC calculation geometry model.</p>
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<p>Single tamping attenuation diagram.</p>
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<p>Load application method.</p>
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<p>Comparison of soil vibration velocity: (<b>a</b>) 30 m from the tamping point; (<b>b</b>) 75 m from the tamping point.</p>
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<p>Comparison chart of tamping settlement.</p>
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<p>The monitoring point sketch map.</p>
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<p>Vibration velocity outside the isolation trench: (<b>a</b>) east–west direction; (<b>b</b>) north–south direction.</p>
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<p>Vibration velocity and <span class="html-italic">A<sub>RF</sub></span> of a 2 m deep isolation trench: (<b>a</b>) east–west direction; (<b>b</b>) north–south direction.</p>
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<p>Vibration velocity and <span class="html-italic">A<sub>RF</sub></span> of an isolation trench located 60 m away from the tamping point: (<b>a</b>) east–west direction; (<b>b</b>) north–south direction.</p>
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<p>Vibration velocity outside the isolation trench for filling materials with different unit weights: (<b>a</b>) east–west direction; (<b>b</b>) north–south direction.</p>
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<p>Vibration velocity outside the isolation trench for different damping ratios of the filling material: (<b>a</b>) east–west direction; (<b>b</b>) north–south direction.</p>
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<p>Vibration velocity outside the isolation trench for different cohesion and friction angles of the filling material: (<b>a</b>) east–west direction; (<b>b</b>) north–south direction.</p>
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<p>Vibration velocity outside the isolation trench for different stiffness and spacing of spring dampers: (<b>a</b>) east–west direction; (<b>b</b>) north–south direction.</p>
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21 pages, 11485 KiB  
Article
Numerical Investigation on Deep-Foundation Pit Excavation Supported by Box-Type Retaining Walls
by Peng Peng, Weiyao Kong, Saishuai Huang, Yi Long and Yang Lu
Buildings 2025, 15(1), 109; https://doi.org/10.3390/buildings15010109 - 31 Dec 2024
Viewed by 443
Abstract
In soft soil foundations, the utilization of box-type retaining walls as a support method represents a novel approach. This study focuses on investigating the key factors influencing lateral wall deflection and ground settlement behind the wall in deep excavation projects supported by box-type [...] Read more.
In soft soil foundations, the utilization of box-type retaining walls as a support method represents a novel approach. This study focuses on investigating the key factors influencing lateral wall deflection and ground settlement behind the wall in deep excavation projects supported by box-type retaining walls. Based on a practical engineering case in Shanghai, the large deformation Lagrangian numerical simulation software FLAC-3D is employed to simulate the displacement of box-type retaining walls as well as the surface settlement surrounding the excavation pit during the excavation process of deep-foundation pits. This research encompasses aspects such as the box size, the filling material within the box, and the constituent materials of the retaining wall. Ultimately, it is concluded that variations in the size of the box-retaining wall have a significant impact on wall deflection and surrounding ground settlement, while the filling material and constituent materials have relatively minor effects. This study provides a theoretical basis and scientific reference for the design and construction of box-type retaining walls in deep-foundation pit engineering. Full article
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<p>Location of the considered project: (<b>a</b>) picture of foundation pit zoning; (<b>b</b>) graphic layout of foundation pit zoning.</p>
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<p>Construction site images: (<b>a</b>) Excavation of pit inside box-type retaining wall; (<b>b</b>) Excavation construction of the foundation pit to the bottom; (<b>c</b>) Completed box-type retaining wall; (<b>d</b>) Completed foundation pit site; (<b>e</b>) Schematic diagram for lateral deformation (inclinometry) monitoring of retaining walls.</p>
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<p>(<b>a</b>) The cross-section of the foundation pit with box-type retaining wall. (<b>b</b>) Soil profiles and material properties at the site.</p>
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<p>(<b>a</b>) The cross-section of the foundation pit with box-type retaining wall. (<b>b</b>) Soil profiles and material properties at the site.</p>
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<p>Numerical simulation model. (<b>a</b>) FLAC 3D calculation model of the whole foundation pit. (<b>b</b>) Model boundary conditions.</p>
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<p>Detailed numerical simulation model. (<b>a</b>) Underground diaphragm wall. (<b>b</b>) Back wall of box-type retaining wall. (<b>c</b>) Three-axis mixing pile. (<b>d</b>) Bored pile.</p>
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<p>Comparison of measured and simulated deformations at measurement location of the front wall of the box-type retaining wall displacement.</p>
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<p>(<b>a</b>) Settlement curve of the foundation pit. (<b>b</b>) The influence zone behind the wall.</p>
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<p>(<b>a</b>) Settlement curve of the foundation pit. (<b>b</b>) The influence zone behind the wall.</p>
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<p>Settlement cloud map after excavation at different steps: (<b>a</b>) first layer excavation; (<b>b</b>) second layer excavation; (<b>c</b>) third layer excavation.</p>
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<p>(<b>a</b>) Numerical simulation of soil settlement curve around foundation pit; (<b>b</b>) schematic diagram of the distance from the edge of the pit.</p>
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<p>Displacement cloud diagram of each supporting structure: (<b>a</b>) Underground diaphragm wall; (<b>b</b>) Back wall of box-type retaining wall; (<b>c</b>) Three-axis mixing pile; (<b>d</b>) Bored pile.</p>
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<p>Influence of box-type retaining wall dimensions: (<b>a</b>,<b>b</b>) Horizontal displacements of front wall of box-type retaining wall; (<b>c</b>,<b>d</b>) Surrounding surface settlements with variations in the box length and width.</p>
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<p>Influence of box-type retaining wall dimensions: (<b>a</b>,<b>b</b>) Horizontal displacements of front wall of box-type retaining wall; (<b>c</b>,<b>d</b>) Surrounding surface settlements with variations in the box length and width.</p>
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<p>Influence of the internal fill material of box-type retaining walls: (<b>a</b>) Horizontal displacement of the front wall of box-type retaining wall; (<b>b</b>) settlement of the surrounding surface from the edge of foundation pit.</p>
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<p>Influence of the internal fill material of box-type retaining walls: (<b>a</b>) Horizontal displacement of the front wall of box-type retaining wall; (<b>b</b>) settlement of the surrounding surface from the edge of foundation pit.</p>
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<p>Influence of concrete materials used for pouring box-type retaining walls: (<b>a</b>) Horizontal displacement of the front wall of box-type retaining wall; (<b>b</b>) settlement of the surrounding surface from the edge of foundation pit.</p>
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<p>Influence of concrete materials used for pouring box-type retaining walls: (<b>a</b>) Horizontal displacement of the front wall of box-type retaining wall; (<b>b</b>) settlement of the surrounding surface from the edge of foundation pit.</p>
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17 pages, 7790 KiB  
Article
Application of UAV-SfM Photogrammetry to Monitor Deformations of Coastal Defense Structures
by Santiago García-López, Mercedes Vélez-Nicolás, Verónica Ruiz-Ortiz, Pedro Zarandona-Palacio, Antonio Contreras-de-Villar, Francisco Contreras-de-Villar and Juan José Muñoz-Pérez
Remote Sens. 2025, 17(1), 71; https://doi.org/10.3390/rs17010071 - 28 Dec 2024
Viewed by 703
Abstract
Coastal defense has traditionally relied on hard infrastructures like breakwaters, dykes, and groins to protect harbors, settlements, and beaches from the impacts of longshore drift and storm waves. The prolonged exposure to wave erosion and dynamic loads of different nature can result in [...] Read more.
Coastal defense has traditionally relied on hard infrastructures like breakwaters, dykes, and groins to protect harbors, settlements, and beaches from the impacts of longshore drift and storm waves. The prolonged exposure to wave erosion and dynamic loads of different nature can result in damage, deformation, and eventual failure of these infrastructures, entailing severe economic and environmental losses. Periodic post-construction monitoring is crucial to identify shape changes, ensure the structure’s stability, and implement maintenance works as required. This paper evaluates the performance and quality of the restitution products obtained from the application of UAV photogrammetry to the longest breakwater in the province of Cádiz, southern Spain. The photogrammetric outputs, an orthomosaic and a Digital Surface Model (DSM), were validated with in situ RTK-GPS measurements, displaying excellent planimetric accuracy (RMSE 0.043 m and 0.023 m in X and Y, respectively) and adequate altimetric accuracy (0.100 m in Z). In addition, the average enveloping surface inferred from the DSM allowed quantification of the deformation of the breakwater and defining of the deformation mechanisms. UAV photogrammetry has proved to be a suitable and efficient technique to complement traditional monitoring surveys and to provide insights into the deformation mechanisms of coastal structures. Full article
(This article belongs to the Special Issue Coastal and Littoral Observation Using Remote Sensing)
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<p>Overview of the study area with indication of the Puntilla breakwater (red rectangle), located at the mouth of the Guadalete river.</p>
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<p>(<b>a</b>) DJI Matrice 210 V2 quadcopter, (<b>b</b>) DJI Zenmuse X4S camera, (<b>c</b>) target used as ground control point, and (<b>d</b>) RTK-dGPS conformed by a Leica GS18 antenna and a Leica CS20 field controller.</p>
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<p>Image of one of the GCPs taken as a reference for its good visibility along the breakwater.</p>
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<p>Workflow followed to characterize the breakwater geometry and generate the model.</p>
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<p>Panoramic view of the breakwater taken on the day of data acquisition where both good weather and sea conditions are observed.</p>
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<p>Flight plan consisting of four path lines (in green) generated with the DJI Pilot software in order to cover the breakwater.</p>
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<p>Detail of the cartographic products at the tip of the breakwater (<b>a</b>) Orthomosaic, (<b>b</b>) DSM.</p>
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<p>Frequency distribution of the residuals in Z in the DSM.</p>
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<p>(<b>a</b>) DSM of the entire breakwater; (<b>b</b>) detail of the smoothed DSM (elevation range between 3.5 and 6.5 m) at the SW end of the breakwater with indication of the 12 crests identified.</p>
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<p>Evolution along the breakwater of the position and height of the crests and troughs identified on the outer façade of the Puntilla breakwater. The origin of distances is located on the first crest.</p>
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<p>Picture taken on 26 March 2024 during a westerly storm showing the breaking of 5 wave crests (indicated in the image) affecting the outer facade of the breakwater, in the 300 m-long section where the crest-trough morphologies can be identified.</p>
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19 pages, 8580 KiB  
Article
Study on the Influence and Deformation Control of Rich Water Foundation Excavation on Adjacent Buildings
by Zhouya Wang, Xiaole Shen, Xiaoxu Tian, Zhanping Song and Pengyuan Zhou
Buildings 2025, 15(1), 52; https://doi.org/10.3390/buildings15010052 - 27 Dec 2024
Viewed by 404
Abstract
Taking the foundation pit of the Suzhou Chunshenhu Road Expressway Reconstruction Project as an example, the excavation process of the foundation pit was numerically simulated using a three-dimensional finite element method. The measured data and simulated data of the lateral deformation of the [...] Read more.
Taking the foundation pit of the Suzhou Chunshenhu Road Expressway Reconstruction Project as an example, the excavation process of the foundation pit was numerically simulated using a three-dimensional finite element method. The measured data and simulated data of the lateral deformation of the enclosure structure, surface settlement deformation of the ground outside the pit, and settlement deformation of the building were compared to analyze the impact of foundation pit construction on adjacent buildings. The influence of foundation pit floor and diaphragm wall thickness on wall displacement, building settlement, and foundation pit uplift was also discussed. The results showed the following: (1) Adding a foundation pit floor has a significant effect on reducing the lateral displacement of the diaphragm wall, settlement of the building, and uplift of the foundation pit. Increasing the thickness of the foundation pit floor has a limited effect on reducing the displacement, while increasing the thickness of the diaphragm wall has a small effect. (2) The displacement curve of the underground diaphragm wall increases with depth. It reaches a maximum at the excavation surface and then decreases gradually. (3) The surface settlement increases first and then decreases with distance from the foundation pit, showing a concave shape. As the depth of excavation increases, the settlement value increases. (4) Through analysis of the monitoring data of vertical displacement of buildings, it can be seen that during foundation pit excavation, buildings undergo five stages: initial slow descent, steep descent, mid-term slow descent, late steep descent, and stable deformation. The buildings are dominated by settlement deformation. Full article
(This article belongs to the Section Building Structures)
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<p>Foundation pit location and site.</p>
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<p>Geological section of the foundation pit.</p>
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<p>Three-dimensional finite element model.</p>
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<p>Cross-section deformation diagram under different working conditions: (<b>a</b>) Condition 1; (<b>b</b>) Condition 2; (<b>c</b>) Condition 3; (<b>d</b>) Condition 4; (<b>e</b>) Condition 5; (<b>f</b>) Condition 6; (<b>g</b>) Condition 7; (<b>h</b>) Condition 8; (<b>i</b>) Condition 9.</p>
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<p>Underground continuous wall lateral displacement under different working conditions.</p>
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<p>Building settlement under different working conditions.</p>
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<p>Uplift deformation at the bottom of the foundation.</p>
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<p>Schematic diagram of internal forces in support structures under different working conditions: (<b>a</b>) Condition 1; (<b>b</b>) Condition 2; (<b>c</b>) Condition 3; (<b>d</b>) Condition 4; (<b>e</b>) Condition 5; (<b>f</b>) Condition 6; (<b>g</b>) Condition 7; (<b>h</b>) Condition 8; (<b>i</b>) Condition 9.</p>
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<p>Schematic diagram of internal forces in support structures under different working conditions: (<b>a</b>) Condition 1; (<b>b</b>) Condition 2; (<b>c</b>) Condition 3; (<b>d</b>) Condition 4; (<b>e</b>) Condition 5; (<b>f</b>) Condition 6; (<b>g</b>) Condition 7; (<b>h</b>) Condition 8; (<b>i</b>) Condition 9.</p>
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<p>Local measurement point layout diagram.</p>
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<p>Lateral deformation of retaining structure: (<b>a</b>) the maximum lateral displacement of the monitoring point and the corresponding depth and (<b>b</b>) the lateral displacement of the monitoring points at different depths.</p>
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<p>Surface settlement deformation outside the pit: (<b>a</b>) settlement changes over time on the south side of the pit and (<b>b</b>) settlement changes over time on the north side of the pit.</p>
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<p>Settlement deformation of the building: (<b>a</b>) absolute settlement at corners and (<b>b</b>) differential settlement along building edges.</p>
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15 pages, 14179 KiB  
Article
Model Testing and Numerical Simulation of the Bearing Characteristics of Screw-Core Cement Mixing Pile
by Luoan Wu, Yue Gao, Yaohui Du, Junjie Xuan, Jiu Nao, Shibo Li, Jinhao Li, Yanqi Wang, Hao Zhang, Lei Cao, Cheng Meng and Zewei Yang
Buildings 2025, 15(1), 41; https://doi.org/10.3390/buildings15010041 - 26 Dec 2024
Viewed by 349
Abstract
The screw-core mixing pile, which enhances traditional smooth-surface rigid piles by introducing a threaded surface, has been rapidly applied in China. Indoor model testing and numerical simulation techniques are used to perform static load tests on single piles to analyze the load–settlement relationship [...] Read more.
The screw-core mixing pile, which enhances traditional smooth-surface rigid piles by introducing a threaded surface, has been rapidly applied in China. Indoor model testing and numerical simulation techniques are used to perform static load tests on single piles to analyze the load–settlement relationship between the new screw-core mixing pile and the traditional circular-core mixing pile. The study examines the axial force distribution between the pile core and the mixing pile shell and establishes a bearing capacity model for screw-core mixing piles. Additionally, model piles with six different thread height ratios (w/d, where w is the thread width and d is the internal diameter of the screw-core) are developed using finite element simulation software to analyze the effect of thread height ratio on the bearing capacity of screw-core mixing piles. The influence of the height ratio on the bearing capacity of screw-core mixing piles is discussed in detail. The results indicate the following: (1) Due to differences in the pile core structure, the bearing capacity of the screw-core mixing pile is 1.44 times greater than that of the circular-core mixing pile. (2) When the vertical load is small, both the pile core and the mixing pile shell share the load; however, as the vertical load increases, the axial force gradually concentrates in the pile core, with the screw core showing a higher load-bearing capacity than the circular-core. (3) Under vertical load, the settlement of the screw-core mixing pile decreases stepwise from the top of the pile down to the surrounding area, demonstrating that the screw-core is more effective than the circular core. (4) The increase in thread height ratio significantly enhances the bearing capacity of the screw-core mixing pile. However, considering material limitations and engineering costs, the optimal thread height ratio should be determined based on actual bearing capacity requirements and soil conditions. Full article
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<p>Samples of unconfined compressive test.</p>
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<p>Model piles.</p>
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<p>Pile cores.</p>
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<p>Model test system: (<b>a</b>) test schematic and (<b>b</b>) test scene.</p>
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<p>Core modeling.</p>
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<p>Numerical modeling.</p>
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<p>Comparison of results between joint simulation and model test.</p>
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<p>Pile cores with different thread height ratios.</p>
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<p>Load–settlement curve.</p>
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<p>Axial force distribution curve of pile core.</p>
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<p>Axial force distribution curve of mixing pile shell.</p>
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<p>Schematic of pile core force. (Q<sub>1</sub> represents the upper load, Q<sub>2</sub> represents the supporting force).</p>
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<p>Settlement cloud of single pile with different w/d (<span class="html-italic">p</span> = 1.25 kN).</p>
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<p>Curve of p-s relationship for different w/d.</p>
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