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Search Results (1,512)

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25 pages, 3300 KiB  
Article
An LCA Study of Various Office Building Shapes Focusing on Operational Energy—A Case of Hamburg
by Samira Shokouhi and Ingo Weidlich
Sustainability 2025, 17(4), 1659; https://doi.org/10.3390/su17041659 - 17 Feb 2025
Viewed by 190
Abstract
The design and configuration of buildings can play a major role in influencing the environmental impacts of the built environment. This paper explores the relation of building shape and it’s environmental impacts by employing a life cycle assessment (LCA) framework. The primary objective [...] Read more.
The design and configuration of buildings can play a major role in influencing the environmental impacts of the built environment. This paper explores the relation of building shape and it’s environmental impacts by employing a life cycle assessment (LCA) framework. The primary objective is to contribute to the ongoing discourse on sustainable construction practices by exploring alternatives in office building shapes and heights. The initial focus of our study centers on a set of plan shapes based on different combinations of a 12 × 14 square meter modular unit. This set introduces variations with and without courtyards, coupled with three distinct heights of 3, 6, and 12 m (1, 2, and 4 stories). Expanding our exploration, we introduce a second set of standard geometric shapes, namely square, pentagon, hexagon, heptagon, octagon, and circle. We assess the annual energy demand of buildings with these plan shapes and conduct an LCA analysis focused on the operational energy use stage in the eLCA tool to quantify their environmental implications, focusing on global warming potential (GWP) and primary energy non-renewable total (PENRT) indicators. Through calculations and comparisons of the LCA results, this paper provides insights into the environmental trade-offs and benefits associated with different building plan shapes and heights. Full article
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<p>First set of shape alternatives with dimensions based on a base 12 × 14 m<sup>2</sup> unit.</p>
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<p>Second set of shape alternatives with dimensions with a fixed area of 1000 m<sup>2</sup>.</p>
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<p>The GWP (kg CO<sub>2</sub> equiv./m<sup>2</sup>NFA·a) of one-story building shapes.</p>
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<p>The GWP (kg CO<sub>2</sub> equiv./m<sup>2</sup>NFA·a) of different building shapes with three different heights.</p>
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<p>The GWP (kg CO<sub>2</sub> equiv./m<sup>2</sup>NFA·a) of different building shapes.</p>
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<p>The PENRT (MJ/m<sup>2</sup>NFA·a) of different building shapes with three different heights.</p>
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<p>The PENRT (MJ/m<sup>2</sup>NFA·a) of different building shapes.</p>
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18 pages, 4228 KiB  
Article
Evaluation of Energy Demands and Performance of Multi-Storey Cross-Laminated Timber Buildings
by Timothy O. Adekunle
Energies 2025, 18(4), 933; https://doi.org/10.3390/en18040933 - 15 Feb 2025
Viewed by 267
Abstract
The overarching goal of this research is to evaluate the energy demands and performance of multi-storey cross-laminated timber (CLT) buildings. The research examines the various energy demands influencing the performance of multi-storey CLT buildings. The study addresses the following research question: Can different [...] Read more.
The overarching goal of this research is to evaluate the energy demands and performance of multi-storey cross-laminated timber (CLT) buildings. The research examines the various energy demands influencing the performance of multi-storey CLT buildings. The study addresses the following research question: Can different energy demands influence the performance of CLT buildings? The investigation explores building modeling and simulation under two different weather scenarios to assess these issues. The study considers London Islington and St Albans (Test Reference Year—TRY), due to the proximity of the actual case studies to the reference locations of the weather files. The investigation captures energy demands and performance in the warm season (i.e., May–August). The findings show that the Stadt building (STB) temperatures under the two weather scenarios are warmer by 1.2 °C and 1.6 °C than those of Brid building (BDH) under the same weather conditions. Outdoor dry-bulb temperatures have a lesser impact on radiant temperatures than indoor air temperatures and operative temperatures in the buildings. Solar gains for external windows are influenced by design variables (e.g., building shapes, heights, floor areas, orientations, opening sizes, etc.). The indoor environmental conditions of the buildings under different weather conditions are comfortable, except for BDH St Albans TRY. Occupancy is a major driver influencing domestic hot water (DHW) usage profiles, regardless of the energy sources in the buildings. DHW is a significant parameter determining the overall energy usage in buildings. Other energy usage profiles, such as room electricity, computers and equipment, general lighting, and lighting, can also impact energy usage in buildings. The research outcomes can enhance our understanding of energy usage profiles and possible improvements to enhance the overall performance of CLT buildings. Full article
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<p>Averages for maximum, mean, and minimum monthly temperatures in study area.</p>
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<p>The ground floor plan of BDH, with red circles showing some of the units that were monitored during the indoor monitoring.</p>
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<p>One of the units measured on the ground floor of BDH, with the sensor placed on the wall at 1.1 m above the floor level. The red circle shows the sensor’s location.</p>
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<p>Correlations between outdoor dry-bulb temperatures and indoor environmental variables for BDH and STB London Islington TRYs.</p>
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<p>Correlations between outdoor dry-bulb temperatures and indoor environmental variables for BDH and STB St Albans TRY.</p>
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<p>Correlations between occupancy, room electricity, and lighting for BDH and STB London Islington.</p>
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<p>Correlations between occupancy, room electricity, and lighting for BDH and STB St Albans.</p>
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<p>Regressions between occupancy and DHW (gas) for BDH and STB London Islington.</p>
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<p>Regressions between occupancy and DHW (gas) for BDH and STB St Albans.</p>
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<p>Minimum, average, and maximum values of variables for BDH and STB London Islington.</p>
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<p>Minimum, average, and maximum values of variables for BDH and STB St Albans.</p>
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<p>Radar comparison of lowest, mean, and highest values of variables’ usage profiles for BDH and STB London Islington.</p>
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<p>Radar comparison of lowest, mean, and highest values of variables’ usage profiles for BDH and STB St Albans.</p>
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<p>Cumulative values of total averages of lowest, mean, and highest values of variables for BDH London Islington.</p>
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19 pages, 4026 KiB  
Article
Parametric Numerical Analysis of Factors Influencing the Shear Strength of Precast Concrete Walls with Dry Connections
by Aléxia Ribeiro, Panagiotis Daskalakis, Seyedsajjad Hosseini and André Furtado
Appl. Sci. 2025, 15(4), 1959; https://doi.org/10.3390/app15041959 - 13 Feb 2025
Viewed by 347
Abstract
Precast concrete is an advanced construction technique characterised by high precision, quality, optimisation and is increasingly used in commercial and residential buildings. However, connections between precast elements are often constructed using in-situ casting, which can delay projects and complicate disassembly at the end [...] Read more.
Precast concrete is an advanced construction technique characterised by high precision, quality, optimisation and is increasingly used in commercial and residential buildings. However, connections between precast elements are often constructed using in-situ casting, which can delay projects and complicate disassembly at the end of a structure’s service life. Dry connections, aligned with the principles of manufacture-to-assemble (MTA), offer a practical and sustainable alternative but present significant challenges regarding seismic performance, particularly in earthquake-prone regions. This study addresses these challenges through a comprehensive parametric numerical investigation into the shear capacity of precast walls with dry connections. Using SeismoStruct 2024 software, more than 340 pushover simulations were conducted to evaluate the influence of various parameters, including concrete compressive strength, axial force percentage, wall section height, overall wall height, and connection characteristics such as bar diameter, quantity, and placement. This research provides critical insights into the combined effects of these parameters, identifying optimal configurations to maximise shear capacity, which is a vital factor for seismic performance. Key findings indicate that shear capacity is significantly enhanced by increasing section height, concrete strength, and axial load, with notable gains such as an 84% improvement in shear strength when section height increased from 2 m to 3 m under favourable conditions. Conversely, increasing overall wall height tended to reduce shear capacity, with a 58% decrease observed for walls extending from 1.5 m to 3.5 m. Adjustments in mechanical connections, including larger diameters, increased bar quantities, and optimised placements, further contributed to incremental improvements in shear strength, with increases ranging from 3% to 24%. Full article
(This article belongs to the Section Civil Engineering)
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<p>Wall modelling strategy.</p>
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<p>(<b>a</b>) Scheme of the experimental specimen, adapted from [<a href="#B15-applsci-15-01959" class="html-bibr">15</a>] (<b>b</b>) Numerical results compared with the experiments adapted from [<a href="#B16-applsci-15-01959" class="html-bibr">16</a>].</p>
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<p>Identification of the geometric parameters studied (<b>a</b>) Wall height (H) and Section height (hc) (<b>b</b>) Two rebars configuration (<b>c</b>) Three rebars configuration (<b>d</b>) Five rebars configuration centred (<b>e</b>) Five rebars configuration with edge placement.</p>
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<p>3D plots: Maximum Shear as a function of concrete compressive strength (fck) and normalised axial force (v) for: (<b>a</b>) hc = 2.00 m (<b>b</b>) hc = 2.25 m (<b>c</b>) hc = 2.50 m (<b>d</b>) hc = 2.75 m (<b>e</b>) hc = 3.00 m.</p>
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<p>Influence of Concrete Compressive Strength on Maximum Shear Capacity for Different Normalised Axial Loads: (<b>a</b>) Global Trends for all Levels of Axial Load, (<b>b</b>) Magnified view for v = 0.8, (<b>c</b>) Magnified view for v = 0.2, (<b>d</b>) Magnified View for v = 0.0.</p>
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<p>Normalised axial forces curves × Maximum shear for different compressive concrete strength (<b>a</b>) Global Trends for all concrete grades, (<b>b</b>) Magnified view for fck = 50 MPa, (<b>c</b>) Magnified view for fck = 35 MPa, (<b>d</b>) Magnified view for fck = 20 MPa.</p>
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<p>Maximum shear—Section height curves (<b>a</b>) Global Trends for all Section Heights, (<b>b</b>) Magnified view for v = 0.0, (<b>c</b>) Magnified view for v = 0.4, (<b>d</b>) Magnified view for v = 0.8.</p>
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<p>Influence of the section height: Shear Increment-Normalised axial force curves (<b>a</b>) hc = 2.00 m (<b>b</b>) hc = 2.25 m (<b>c</b>) hc = 2.50 m (<b>d</b>) hc = 2.75 m (<b>e</b>) hc = 3.00 m.</p>
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<p>(<b>a</b>) Wall height curve for fck = 30 MPa, νd = 0.4 (<b>b</b>) magnified view.</p>
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<p>The influence of bar sizes (<b>a</b>) Global Trends for all Section Heights, (<b>b</b>) Magnified view for hc = 1.5 m, (<b>c</b>) Magnified view for hc = 2.25 m, (<b>d</b>) Magnified view for hc = 2.5 m.</p>
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<p>Influence of the number and position of the bars (<b>a</b>) Global Trends for all Section Heights, (<b>b</b>) Magnified view for hc = 1.5 m (<b>c</b>) Magnified view for hc = 2.25 m, (<b>d</b>) Magnified view for hc = 2.5 m.</p>
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22 pages, 7659 KiB  
Article
Slab-to-Column Seismic Pounding Between Multistorey Buildings: Influence of the Impact Point Location and the Pre-Existing Gap Size
by Grigorios Manoukas and Chris Karayannis
Buildings 2025, 15(4), 581; https://doi.org/10.3390/buildings15040581 - 13 Feb 2025
Viewed by 321
Abstract
The present paper deals with the asymmetric seismic interaction phenomenon between multistorey reinforced concrete buildings. The paper focuses on the so-called floor-to-column pounding and aims to identify the influence of two specific factors: the exact impact point location and the width of the [...] Read more.
The present paper deals with the asymmetric seismic interaction phenomenon between multistorey reinforced concrete buildings. The paper focuses on the so-called floor-to-column pounding and aims to identify the influence of two specific factors: the exact impact point location and the width of the pre-existing separation gap between the interacting structures. Furthermore, the estimation of the effective impact length, i.e., the part of the external columns directly suffering the hit within their clear height that experiences severe damage, is attempted. For this purpose, several interaction cases are analyzed by means of inelastic dynamic analysis, and representative response quantities are calculated. In addition, a well-documented analytical procedure is applied in order to determine the effective impact length. The whole investigation highlights the crucial role of the impact point location for the local response of the external columns. On the contrary, it demonstrates that the overall building behavior is not considerably affected. In addition, it reveals that the existence of inadequate seismic joints may be more unfavorable in comparison with the complete absence of separation between the interacting structures. Thus, the relevant code provisions imposing a minimum seismic joint width should be strictly abided by. Finally, the investigation confirms field observations and experimental results which indicate that the damage of external columns which undergo strong pounding forces is limited to a short area with length equal to about 1 m or less. Due attention should be given to this area during retrofitting of existing buildings. Full article
(This article belongs to the Special Issue Challenges in Seismic Analysis and Assessment of Buildings)
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<p>Distinction between (<b>a</b>) symmetric and (<b>b</b>) asymmetric seismic interaction. Outline of the plan view of interacting buildings.</p>
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<p>Distinction between (<b>a</b>) type A (floor-to-floor) and (<b>b</b>) type B (floor-to-column) pounding. Outline of the elevation view of interacting buildings.</p>
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<p>Definition of the theoretical impact point height h<sub>i</sub> in a finite element structural analysis model.</p>
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<p>Definition of L<sub>eff</sub>: (<b>a</b>) qualitative shear force diagram of a column suffering pounding force within its clear height; (<b>b</b>) shear damage of an external column due to pounding after the strong earthquake in Alkyonides, Greece, in 1981; (<b>c</b>) effective impact length L<sub>eff</sub>.</p>
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<p>Eight-storey reinforced concrete buildings: (<b>a</b>) plan view; (<b>b</b>) outline of the view in elevation.</p>
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<p>One-, three- and six-storey buildings: (<b>a</b>) plan view of buildings “3” and “6”; (<b>b</b>) outline of the view in elevation.</p>
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<p>Contact conditions between the interacting buildings: (<b>a</b>) layout of the interacting buildings; (<b>b</b>) enlargement of the contact area.</p>
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<p>Alternative values of h<sub>i</sub> and d<sub>sj</sub>.</p>
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<p>Maximum absolute shear forces of column Κ4 along X axis due to excitation “1+”: (<b>a</b>) P1ipl; (<b>b</b>) I1ipl; (<b>c</b>) I3ipl; (<b>d</b>) I6ipl.</p>
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<p>Time history of shear forces of column Κ4 along the X axis at the top of the first storey due to the first 20 s of excitation “1+”. Analysis series P1ipl: (<b>a</b>) no pounding; (<b>b</b>) h<sub>i</sub> = h/2; (<b>c</b>) h<sub>i</sub> = 2h/3; (<b>d</b>) h<sub>i</sub> = 3h/4.</p>
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<p>Maximum absolute plastic rotation demands of column Κ4 around Y axis due to excitation “1-”: (<b>a</b>) P1ipl; (<b>b</b>) I6ipl.</p>
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<p>Minimum and maximum (<b>a</b>) floor translations along X axis; (<b>b</b>) floor rotations around Z axis; (<b>c</b>) storey drifts along X axis. Analysis series I6ipl = excitation “1-”.</p>
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<p>Maximum absolute shear forces of column Κ4 along X axis due to excitations: (<b>a</b>) “1+”; (<b>b</b>) “1-”; (<b>c</b>) “2+”; (<b>d</b>) “2-”. Analysis series P1sjw.</p>
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<p>Time history of shear forces of column Κ4 along the X axis at the top of the third storey due to the first 20 s of excitation “1-”. Analysis series I3sjw: (<b>a</b>) d<sub>sj</sub> = 0 cm; (<b>b</b>) d<sub>sj</sub> = 1 cm; (<b>c</b>) d<sub>sj</sub> = 2 cm; (<b>d</b>) d<sub>sj</sub> = 3 cm.</p>
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<p>Maximum absolute plastic rotation demands of column Κ4 around Y axis due to excitation “1-”: (<b>a</b>) P1sjw; (<b>b</b>) I1sjw.</p>
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<p>Minimum and maximum (<b>a</b>) floor translations along X axis; (<b>b</b>) floor rotations around Z axis; (<b>c</b>) storey drifts along X axis. Analysis series I3sjw = excitation “1-”.</p>
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<p>Minimum and maximum (<b>a</b>) floor translations along X axis; (<b>b</b>) floor rotations around Z axis; (<b>c</b>) storey drifts along X axis. Analysis series I3sjw = excitation “1-”.</p>
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<p>Time histories of pounding forces acting on the third storey of column Κ4 for interaction cases: (<b>a</b>) “P3-1+”; (<b>b</b>) “I3-2-”.</p>
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<p>Time histories of pounding force acting on the third storey and displacements of characteristic points of column Κ4 for interaction case “P3-1+”.</p>
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<p>Deformation of column K4 in the third storey at discrete time points around the moment that the pounding force is maximized (case “P3-1+”).</p>
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20 pages, 5248 KiB  
Article
Dynamics Modeling and Analysis of Rotating Trapezoidal Flexible Plate System with Large Deformation
by Yongbin Guo, Xian Guo, Ming Li, Jing Zhang, Dingguo Zhang and Jiajun Wu
Aerospace 2025, 12(2), 135; https://doi.org/10.3390/aerospace12020135 - 11 Feb 2025
Viewed by 286
Abstract
Origami-derived space-deployable structures have a broad application prospect in the aerospace field owing to their excellent morphology transformation performance, and they are usually large-scale and lightweight. However, their deformation increases greatly under high-speed and extreme-temperature conditions, which affects their motion and performance and [...] Read more.
Origami-derived space-deployable structures have a broad application prospect in the aerospace field owing to their excellent morphology transformation performance, and they are usually large-scale and lightweight. However, their deformation increases greatly under high-speed and extreme-temperature conditions, which affects their motion and performance and possibly causes losses. So, it is crucial to perform a dynamic analysis considering key factors for the large deformation of flexible structures. In this paper, the Nodal Coordinate-based Floating Frame of Reference (NCFFR) formulation is used to build a rigid–flexible coupling dynamic model of the rotating trapezoidal flexible plate with a Miura angle. NCFFR can not only accurately describe the large deformation of flexible structures but also decouple the overall motion and flexible deformation motion naturally, and it has a potential application in vibration control and large deformation problems for flexible systems. Finally, the key structural parameters (such as Miura angle, trapezoidal plate height, and trapezoidal plate length) are adopted to analyze the dynamic characteristics of the flexible plate system. The simulations reveal that the Miura angle significantly affects the dynamic characteristics of the trapezoidal flexible plate system. The complex “loci veering” phenomenon is captured, with mode shifts between different modal frequencies. As the Miura angle increases, the peak acceleration when the Miura angle is 95° is notably larger than the others, and when the flexible plate is in the stage of uniform rotation, the peak velocity at which the Miura angle is 80° is significantly greater than that of 85° and 75°. The structural parameters (bottom length, height, thickness) have diverse influences on the modal characteristics of the trapezoidal flexible plate. Full article
(This article belongs to the Special Issue Spacecraft Dynamics and Control (2nd Edition))
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<p>The flexible origami-derived space-deployable structure. (<b>a</b>) Origami-derived deployable structure. (<b>b</b>) Schematics of origami-derived space-deployable structure.</p>
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<p>Simplified rotating flexible plate considering Miura angle.</p>
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<p>The schematic of a rotating flexible plate considering the Miura angle. (<b>a</b>) The vector of point <span class="html-italic">P</span> on the flexible plate. (<b>b</b>) The flexible plate in a floating frame of reference.</p>
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<p>ANCF element of flexible plate. (<b>a</b>) ANCF element mesh of flexible plate. (<b>b</b>) ANCF element of flexible plate under different configurations.</p>
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<p>Model of hub-rotating trapezoidal flexible plate.</p>
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<p>The transverse deformation of the rectangular flexible plate at point B.</p>
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<p>Variation in first six nature frequencies with dimensionless rotational speed. (<b>a</b>) When Miura angle is 65°. (<b>b</b>) When Miura angle is 75°. (<b>c</b>) When Miura angle is 80°. (<b>d</b>) When Miura angle is 85°. (<b>e</b>) When Miura angle is 95°.</p>
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<p>Variation in first six nature frequencies with dimensionless rotational speed. (<b>a</b>) When Miura angle is 65°. (<b>b</b>) When Miura angle is 75°. (<b>c</b>) When Miura angle is 80°. (<b>d</b>) When Miura angle is 85°. (<b>e</b>) When Miura angle is 95°.</p>
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<p>The fourth- and fifth-mode pitch lines of the rotational trapezoidal flexible plate when the Miura angle is 85°. (<b>a</b>) The fourth mode. (<b>b</b>) The fifth mode.</p>
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<p>The fourth- and fifth-mode pitch lines of the rotational trapezoidal flexible plate when the Miura angle is 85°. (<b>a</b>) The fourth mode. (<b>b</b>) The fifth mode.</p>
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<p>The tip transverse deformation of the trapezoidal flexible plate. (<b>a</b>) The transverse deformation of point <span class="html-italic">A</span>. (<b>b</b>) The transverse deformation of point <span class="html-italic">B</span>.</p>
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<p>The tip transverse velocity of the trapezoidal flexible plate. (<b>a</b>) The transverse velocity at point <span class="html-italic">A</span>. (<b>b</b>) The transverse velocity at point <span class="html-italic">B</span>.</p>
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<p>The tip transverse acceleration of the trapezoidal flexible plate. (<b>a</b>) The transverse acceleration at point <span class="html-italic">A</span>. (<b>b</b>) The transverse acceleration at point <span class="html-italic">B</span>.</p>
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20 pages, 4935 KiB  
Article
An Analytical Model for the Steady-State Thermal Analysis of Façade-Integrated PV Modules Cooled by a Solar Chimney
by Marko Šućurović, Dardan Klimenta, Darius Andriukaitis, Mindaugas Žilys, Tomyslav Sledevič and Milan Tomović
Appl. Sci. 2025, 15(3), 1664; https://doi.org/10.3390/app15031664 - 6 Feb 2025
Viewed by 516
Abstract
This paper proposes a steady-state thermal model for the passive cooling of photovoltaic (PV) modules integrated into a vertical building façade by means of a solar chimney, including an empirical correlation for turbulent free convection from a vertical isothermal plate. The proposed analytical [...] Read more.
This paper proposes a steady-state thermal model for the passive cooling of photovoltaic (PV) modules integrated into a vertical building façade by means of a solar chimney, including an empirical correlation for turbulent free convection from a vertical isothermal plate. The proposed analytical model estimates the air velocities at the inlet and at the outlet of the ventilation channel of such a cooling system and the average temperature of the façade-integrated PV modules. A configuration composed of a maximum of six vertically installed PV modules and one solar chimney is considered. The air velocities at the inlet and at the outlet of the ventilation channel obtained for the case of installing PV modules on the building façade are compared with those calculated for the case where the PV modules are integrated into the roof with a slope of 37°. By comparing each of the solutions with one PV module to the corresponding one with six PV modules, it was found that the increase in the air velocity due to the effects of the solar irradiance and the height difference between the two openings of the ventilation channel ranges between 41.05% in the case of “Roof” and 141.14% in the case of “Façade”. In addition, it was obtained that an increase in the solar chimney height of 1 m leads to a decrease in the average PV section temperature by 1.95–7.21% and 0.65–2.92% in the cases of “Roof” and “Façade”, respectively. Finally, the obtained results confirmed that the use of solar chimneys for passive cooling of façade-integrated PV modules is technically justified. Full article
(This article belongs to the Special Issue Application of Perovskite Solar Cells)
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<p>Heat transfer processes from surfaces of façade-integrated PV modules cooled by solar chimney.</p>
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<p>Comparisons between measured values of temperatures <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>T</mi> </mrow> <mrow> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">V</mi> </mrow> </msub> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>T</mi> </mrow> <mrow> <mi mathvariant="normal">a</mi> </mrow> </msub> </mrow> </semantics></math> and simulated values of temperatures <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>T</mi> </mrow> <mrow> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">V</mi> </mrow> </msub> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>T</mi> </mrow> <mrow> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">V</mi> <mi mathvariant="normal">u</mi> </mrow> </msub> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>T</mi> </mrow> <mrow> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">V</mi> <mi mathvariant="normal">b</mi> </mrow> </msub> </mrow> </semantics></math>, and <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>T</mi> </mrow> <mrow> <mi mathvariant="normal">a</mi> </mrow> </msub> </mrow> </semantics></math>.</p>
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<p>The velocity of the air at the outlet of the solar chimney depending on the solar irradiance for two different numbers of PV modules per section and (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">T</mi> <mi mathvariant="normal">S</mi> </mrow> </msub> <mo>+</mo> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">A</mi> <mi mathvariant="normal">P</mi> </mrow> </msub> <mo>≈</mo> </mrow> </semantics></math> 0.5 m; (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">T</mi> <mi mathvariant="normal">S</mi> </mrow> </msub> <mo>+</mo> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">A</mi> <mi mathvariant="normal">P</mi> </mrow> </msub> <mo>=</mo> </mrow> </semantics></math> 1 m; and (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">T</mi> <mi mathvariant="normal">S</mi> </mrow> </msub> <mo>+</mo> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">A</mi> <mi mathvariant="normal">P</mi> </mrow> </msub> <mo>=</mo> </mrow> </semantics></math> 1.5 m.</p>
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<p>The average temperature of the PV section depending on the solar irradiance for two different numbers of PV modules per section and (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">T</mi> <mi mathvariant="normal">S</mi> </mrow> </msub> <mo>+</mo> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">A</mi> <mi mathvariant="normal">P</mi> </mrow> </msub> <mo>≈</mo> </mrow> </semantics></math> 0.5 m; (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">T</mi> <mi mathvariant="normal">S</mi> </mrow> </msub> <mo>+</mo> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">A</mi> <mi mathvariant="normal">P</mi> </mrow> </msub> <mo>=</mo> </mrow> </semantics></math> 1 m; and (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">T</mi> <mi mathvariant="normal">S</mi> </mrow> </msub> <mo>+</mo> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">A</mi> <mi mathvariant="normal">P</mi> </mrow> </msub> <mo>=</mo> </mrow> </semantics></math> 1.5 m.</p>
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<p>Fundamental dimensionless number for free convection depending on solar irradiance for two different numbers of PV modules per section and <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">T</mi> <mi mathvariant="normal">S</mi> </mrow> </msub> <mo>+</mo> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">A</mi> <mi mathvariant="normal">P</mi> </mrow> </msub> <mo>≈</mo> </mrow> </semantics></math> 0.5 m, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">T</mi> <mi mathvariant="normal">S</mi> </mrow> </msub> <mo>+</mo> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">A</mi> <mi mathvariant="normal">P</mi> </mrow> </msub> <mo>=</mo> </mrow> </semantics></math> 1 m, and <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">T</mi> <mi mathvariant="normal">S</mi> </mrow> </msub> <mo>+</mo> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">A</mi> <mi mathvariant="normal">P</mi> </mrow> </msub> <mo>=</mo> </mrow> </semantics></math> 1.5 m.</p>
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<p>(<b>a</b>) The velocity of the air at the outlet of the solar chimney and (<b>b</b>) the average temperature of the PV section depending on the height difference between the two openings of the ventilation channel for two different numbers of PV modules. Note: For the case of PV modules integrated into the roof, the dimension <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">T</mi> <mi mathvariant="normal">S</mi> </mrow> </msub> <mo>+</mo> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">A</mi> <mi mathvariant="normal">P</mi> </mrow> </msub> <mo>+</mo> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">V</mi> </mrow> </msub> <mo>+</mo> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">B</mi> <mi mathvariant="normal">S</mi> </mrow> </msub> </mrow> </semantics></math> represents the sum of the projections of the corresponding individual lengths <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">T</mi> <mi mathvariant="normal">S</mi> </mrow> </msub> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">A</mi> <mi mathvariant="normal">P</mi> </mrow> </msub> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">P</mi> <mi mathvariant="normal">V</mi> </mrow> </msub> </mrow> </semantics></math>, and <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mi mathvariant="normal">B</mi> <mi mathvariant="normal">S</mi> </mrow> </msub> </mrow> </semantics></math>.</p>
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<p>Fundamental dimensionless number for free convection depending on solar irradiance in assumed steady-state conditions for six different numbers of PV modules per section.</p>
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<p>Power of PV section depending on solar irradiance for six different numbers of (<b>a</b>) roof-integrated and (<b>b</b>) façade-integrated PV modules per section cooled by solar chimney with height of 0.5 m.</p>
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14 pages, 864 KiB  
Article
Power Coefficient for Large Wind Turbines Considering Wind Gradient Along Height
by Saroj Biswas and Jim Shih-Jiun Chen
Energies 2025, 18(3), 740; https://doi.org/10.3390/en18030740 - 6 Feb 2025
Viewed by 483
Abstract
The Betz constant is the well-known aerodynamic limit of the maximum power which can be extracted from wind using wind turbine technologies, under the assumption that the wind speed is uniform across a blade disk. However, this condition may not hold for large [...] Read more.
The Betz constant is the well-known aerodynamic limit of the maximum power which can be extracted from wind using wind turbine technologies, under the assumption that the wind speed is uniform across a blade disk. However, this condition may not hold for large wind turbines, since the wind speed may not be constant along their height; rather, it may vary with the location due to surface friction from tall buildings and trees, the topography of the Earth’s surface, and radiative heating and cooling in a 24 h cycle. This paper derives a new power coefficient for large wind turbines based on the power law exponent model of the wind gradient and height. The proposed power coefficient is a function of the size of the rotor disk and the Hellmann exponent, which describes the wind gradient based on wind stability at various locations, and it approaches the same value as the Betz limit for wind turbines with small rotor disks. It is shown that for large offshore wind turbines, the power coefficient was about 1.27% smaller than that predicted by the Betz limit, whereas for onshore turbines in human-inhabited areas with stable air, the power coefficient was about 8.7% larger. Our results are significant in two ways. First, we achieve generalization of the well-known Betz limit through elimination of the assumption of a constant wind speed across the blade disk, which does not hold for large wind turbines. Second, since the power coefficient depends on the location and air stability, this study offers guidelines for wind power companies regarding site selection for the installation of new wind turbines, potentially achieving greater energy efficiency than that predicted by the Betz limit. Full article
(This article belongs to the Special Issue Recent Developments of Wind Energy)
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<p>Comparison of wind gradient models. Solid line = power law exponent model; dotted line = logarithmic model. (<b>a</b>) Open oceans <math display="inline"><semantics> <mrow> <mo>(</mo> <mi>α</mi> <mo>=</mo> <mn>0.1</mn> <mo>,</mo> <mspace width="0.166667em"/> <msub> <mi>z</mi> <mn>0</mn> </msub> <mo>=</mo> <mn>0.0002</mn> <mo>)</mo> </mrow> </semantics></math>. (<b>b</b>) Neutral air for flat, open coast <math display="inline"><semantics> <mrow> <mo>(</mo> <mi>α</mi> <mo>=</mo> <mn>0.16</mn> <mo>,</mo> <mspace width="0.166667em"/> <msub> <mi>z</mi> <mn>0</mn> </msub> <mo>=</mo> <mn>0.03</mn> <mo>)</mo> </mrow> </semantics></math>. (<b>c</b>) Neutral air in human-inhibited area <math display="inline"><semantics> <mrow> <mo>(</mo> <mi>α</mi> <mo>=</mo> <mn>0.333</mn> <mo>,</mo> <mspace width="0.166667em"/> <msub> <mi>z</mi> <mn>0</mn> </msub> <mo>=</mo> <mn>0.25</mn> <mo>)</mo> </mrow> </semantics></math>. (<b>d</b>) Stable air in human-inhibited area <math display="inline"><semantics> <mrow> <mo>(</mo> <mi>α</mi> <mo>=</mo> <mn>0.6</mn> <mo>,</mo> <mspace width="0.166667em"/> <msub> <mi>z</mi> <mn>0</mn> </msub> <mo>=</mo> <mn>2.0</mn> <mo>)</mo> </mrow> </semantics></math>.</p>
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<p>Schematic of a large wind turbine.</p>
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<p>Power coefficient with Hellmann exponent <math display="inline"><semantics> <mi>α</mi> </semantics></math>.</p>
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<p>Power coefficient as a function of the ratio <math display="inline"><semantics> <mstyle scriptlevel="0" displaystyle="true"> <mfrac> <mi>R</mi> <msub> <mi>h</mi> <mn>0</mn> </msub> </mfrac> </mstyle> </semantics></math>.</p>
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<p>Variation in power density with height for <math display="inline"><semantics> <msub> <mi>V</mi> <mn>0</mn> </msub> </semantics></math> = 10 m/s, <math display="inline"><semantics> <msub> <mi>h</mi> <mn>0</mn> </msub> </semantics></math> = 90 m, and <span class="html-italic">R</span> = 62.5 m.</p>
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<p>Average wind speed at US shoreline at a height of 90 m [<a href="#B30-energies-18-00740" class="html-bibr">30</a>].</p>
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<p>The maximum wind power (MW) as a function of the distance from the shore, with <math display="inline"><semantics> <msub> <mi>V</mi> <mn>0</mn> </msub> </semantics></math> = 8 m/s at the shore, <math display="inline"><semantics> <msub> <mi>V</mi> <mn>0</mn> </msub> </semantics></math> = 10 m/s at 100 km offshore, <math display="inline"><semantics> <msub> <mi>h</mi> <mn>0</mn> </msub> </semantics></math> = 90 m, and <span class="html-italic">R</span> = 62.5 m.</p>
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<p>Power coefficients of various wind turbines in comparison with the Betz limit [<a href="#B32-energies-18-00740" class="html-bibr">32</a>]. Dashed line shows the Betz limit.</p>
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19 pages, 6549 KiB  
Article
Research on the Tunable Optical Alignment Technology of Lidar Under Complex Working Conditions
by Jianfeng Chen, Jie Ji, Chenbo Xie and Yingjian Wang
Remote Sens. 2025, 17(3), 532; https://doi.org/10.3390/rs17030532 - 5 Feb 2025
Viewed by 362
Abstract
Lidar technology is pivotal for detecting and monitoring the atmospheric environment. However, maintaining optical path stability in complex environments poses significant challenges, especially regarding adaptability and cost efficiency. This study proposes a tunable optical alignment method that is applied to the Rotating Rayleigh [...] Read more.
Lidar technology is pivotal for detecting and monitoring the atmospheric environment. However, maintaining optical path stability in complex environments poses significant challenges, especially regarding adaptability and cost efficiency. This study proposes a tunable optical alignment method that is applied to the Rotating Rayleigh Doppler Wind Lidar (RRDWL) to enable precise detection of mid-to-upper atmospheric wind fields. Building on the conventional echo signal strength method, this approach calibrates the signal strength using cloud information and the signal-to-noise ratio (SNR), enabling stratified and tunable optical alignment. Experimental results indicate that the optimized RRDWL achieves a maximum detection height increase from 42 km to nearly 51 km. Additionally, the average horizontal wind speed error at 30 km decreases from 11.3 m/s to 4.4 m/s, with a minimum error of approximately 1 m/s. These findings confirm that the proposed method enhances the effectiveness and reliability of the Lidar system under complex operational and diverse weather conditions. Furthermore, it improves detection performance and provides robust support for applications in related fields. Full article
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<p>Schematic drawing of a bi-axial lidar system, where (<b>a</b>) presents the transmitter and the receiver and (<b>b</b>) the overlap parameters of the emitted laser beam and the field of view of the telescope.</p>
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<p>A visible spike in the SNR trace (caused by strong backscattered signals from the cloud).</p>
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<p>Logic diagram illustrating optical alignment process under different weather conditions.</p>
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<p>Photograph of the RRDWL system overall structure. The system is deployed at Science Island in Hefei, Anhui province, China.</p>
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<p>Total structural deformation, equivalent elastic strain and rotating platform deformation caused by RRDWL rotation.</p>
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<p>Comparison diagram of Lidar echo signal for continuous rotation detection.</p>
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<p>The change of four-line-of-sight Lidar echo signal during continuous rotation.</p>
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<p>Schematic diagram of cross-sweep optical alignment (point A is the initial point and point C is the end point).</p>
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<p>Results of the RRDWL optical alignment test on 12 June 2022.</p>
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<p>Comparison of horizontal wind profiles obtained by RRDWL and Sonde on 23 October 2022.</p>
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<p>Detection of the SNR in four line-of-sight directions of RRDWL in the experiment on 23 October 2022.</p>
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<p>Maximum detection height sequence after RRDWL system optimization. (<b>a</b>) Two edge channels of the F-P interferometer. (<b>b</b>) Total.</p>
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<p>The measurement uncertainty of horizontal wind speed calculated by SNR (i.e., random error caused by optical quantum noise).</p>
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<p>Comparison of horizontal wind speed deviation profiles obtained by RRDWL and Sonde on 23 October 2022.</p>
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<p>Comparison between measured absolute deviation and random error of horizontal wind speed.</p>
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<p>Horizontal wind speed random error sequence at 30 km altitude.</p>
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<p>Absolute deviation of RRDWL measured horizontal wind speed before and after optical alignment optimization.</p>
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26 pages, 3633 KiB  
Article
Forecasting Heat Power Demand in Retrofitted Residential Buildings
by Łukasz Guz, Dariusz Gaweł, Tomasz Cholewa, Alicja Siuta-Olcha, Martyna Bocian and Mariia Liubarska
Energies 2025, 18(3), 679; https://doi.org/10.3390/en18030679 - 1 Feb 2025
Viewed by 361
Abstract
The accurate prediction of heat demand in retrofitted residential buildings is crucial for optimizing energy consumption, minimizing unnecessary losses, and ensuring the efficient operation of heating systems, thereby contributing to significant energy savings and sustainability. Within the framework of this article, the dependence [...] Read more.
The accurate prediction of heat demand in retrofitted residential buildings is crucial for optimizing energy consumption, minimizing unnecessary losses, and ensuring the efficient operation of heating systems, thereby contributing to significant energy savings and sustainability. Within the framework of this article, the dependence of the energy consumption of a thermo-modernized building on a chosen set of climatic factors has been meticulously analyzed. Polynomial fitting functions were derived to describe these dependencies. Subsequent analyses focused on predicting heating demand using artificial neural networks (ANN) were adopted by incorporating a comprehensive set of climatic data such as outdoor temperature; humidity and enthalpy of outdoor air; wind speed, gusts, and direction; direct, diffuse, and total radiation; the amount of precipitation, the height of the boundary layer, and weather forecasts up to 6 h ahead. Two types of networks were analyzed: with and without temperature forecast. The study highlights the strong influence of outdoor air temperature and enthalpy on heating energy demand, effectively modeled by third-degree polynomial functions with R2 values of 0.7443 and 0.6711. Insolation (0–800 W/m2) and wind speeds (0–40 km/h) significantly impact energy demand, while wind direction is statistically insignificant. ANN demonstrates high accuracy in predicting heat demand for retrofitted buildings, with R2 values of 0.8967 (without temperature forecasts) and 0.8968 (with forecasts), indicating minimal performance gain from the forecasted data. Sensitivity analysis reveals outdoor temperature, solar radiation, and enthalpy of outdoor air as critical inputs. Full article
(This article belongs to the Special Issue Energy Efficiency of the Buildings: 3rd Edition)
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<p>Diagram of the conducted analysis presented in this article.</p>
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<p>Forecasting controller: (<b>a</b>) schema of connection forecasting controller installed on existing heat exchanger room; (<b>b</b>) view of forecast controller mounted on tested installation.</p>
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<p>The location of the analyzed multi-family residential building in relation to its surroundings (on the basis of polska.geoportal2.pl (accessed on 10 December 2024) [<a href="#B34-energies-18-00679" class="html-bibr">34</a>]).</p>
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<p>Histogram illustrating the frequency of measured parameters within specified ranges: (<b>a</b>) temperature, (<b>b</b>) air enthalpy, and (<b>c</b>) relative humidity.</p>
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<p>Summary of meteorological data during measurement periods: (<b>a</b>) total radiation, (<b>b</b>) rainfall, (<b>c</b>) wind direction, and (<b>d</b>) wind speed.</p>
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<p>Dependence of the mean outdoor temperature on wind direction by month for the given location.</p>
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<p>Results of measurements: (<b>a</b>) heat energy demand; (<b>b</b>) outdoor temperature.</p>
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<p>Dependence of energy consumption for heating on (<b>a</b>) outdoor air temperature and (<b>b</b>) enthalpy of outdoor air.</p>
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<p>Dependence of heating energy consumption on wind speed determined for each total insolation category.</p>
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<p>Dependence of heating energy consumption on total insolation determined for each wind speed category.</p>
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<p>Dependence of heating energy demand on wind directions according to speed category.</p>
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<p>Comparison of estimated vs. actual demand: top graph uses typical meteorological parameters, and bottom graph includes 1–6 h weather forecasts.</p>
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<p>Comparison of estimated vs. actual demand: top graph uses typical meteorological parameters, and bottom graph includes 1–6 h weather forecasts.</p>
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23 pages, 10445 KiB  
Article
Study on Efficient and Stable Energy Conversion Method of Oscillating Water Column Device Based on Energy Storage Valve Control
by Yunpeng Hai, Zhenyu Yuan, Changdong Wei, Yanjun Liu and Gang Xue
Energies 2025, 18(3), 666; https://doi.org/10.3390/en18030666 - 31 Jan 2025
Viewed by 415
Abstract
Despite extensive research on the performance of Oscillating Water Columns (OWC) over the years, issues with low energy conversion efficiency and unstable power generation have not been addressed. In this study, a novel OWC energy conversion system is proposed based on the working [...] Read more.
Despite extensive research on the performance of Oscillating Water Columns (OWC) over the years, issues with low energy conversion efficiency and unstable power generation have not been addressed. In this study, a novel OWC energy conversion system is proposed based on the working principle of energy storage valve control. The system utilizes accumulators and valve groups to enhance the stability of energy conversion. The hydrodynamic model of the OWC system and the pneumatic model of the novel power take-off (PTO) system are developed using numerical simulations. Building on this, the impact of the incident wave period, wave height, and air chamber opening ratio on the system’s total hydrodynamic performance are examined. The results from the hydrodynamic analysis are subsequently used as input conditions to evaluate the proposed PTO system’s performance. The results show that the hydrodynamic efficiency of the system presents a tendency to increase and then decrease with the increase in the incident wave period, and an optimal period exists. The air chamber opening ratio has a notable influence on the hydrodynamic characteristics of the OWC system, and the larger system damping could be set to achieve a higher capture efficiency in the low-frequency water environment. The incident wave height has a lesser effect on the hydrodynamic characteristics and the resonant period of the device. The designed novel PTO system can effectively improve the energy conversion stability of the OWC device, the flow volatility through the turbine can be reduced by 53.49%, and the output power volatility can be reduced by 25.46% compared with the conventional PTO system. Full article
(This article belongs to the Section D: Energy Storage and Application)
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<p>Diagram of the OWC apparatus.</p>
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<p>Schematic of the novel PTO system: (<b>a</b>) wave rising phase and (<b>b</b>) wave falling phase. 1.1–1.6: Check valves; 2.1, 2.2: accumulators; 3.1, 3.2: switching valves; 4: turbine; 5: generator; and 6: atmosphere.</p>
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<p>Three-dimensional model diagram of the OWC chamber primary structure.</p>
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<p>Sketch of the numerical water flume: (<b>a</b>) front view and (<b>b</b>) top view.</p>
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<p>Comparison of simulation outcomes utilizing various mesh sizes: (<b>a</b>) pressure and (<b>b</b>) weave height.</p>
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<p>Mesh configuration for the numerical wave flume: (<b>a</b>) mesh distribution surrounding the structure (top–down view); (<b>b</b>) mesh distribution surrounding the structure (frontal view); (<b>c</b>) distribution of the mesh along the water depth direction; and (<b>d</b>) general overview of the mesh distribution.</p>
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<p>Overall dimensions of OWC device.</p>
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<p>Comparison chart of simulation results and model experiment results: (<b>a</b>) wave height and (<b>b</b>) pressure.</p>
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<p>Airflow velocity in the OWC device during a wave cycle: (<b>a</b>) 1/4 <span class="html-italic">T</span>; (<b>b</b>) 1/2 <span class="html-italic">T</span>; (<b>c</b>) 3/4 <span class="html-italic">T</span>; and (<b>d</b>) <span class="html-italic">T</span>. (<span class="html-italic">H</span> = 0.2 m; <span class="html-italic">T</span> = 1.5 s).</p>
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<p>Wave surface height in the OWC device during a wave cycle: (<b>a</b>) 1/4 <span class="html-italic">T</span>; (<b>b</b>) 1/2 <span class="html-italic">T</span>; (<b>c</b>) 3/4 <span class="html-italic">T</span>; and (<b>d</b>) <span class="html-italic">T</span>. (<span class="html-italic">H</span> = 0.2 m; <span class="html-italic">T</span> = 1.5 s).</p>
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<p>The wave height versus time inside the air chamber at various incident wave periods.</p>
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<p>The air pressure versus time inside the air chamber at various incident wave periods.</p>
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<p>The airflow velocity at the opening orifice versus time at various incident wave periods.</p>
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<p>The captured power of air chamber versus time at various incident wave periods.</p>
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<p>The hydrodynamic efficiency of the OWC at various incident wave periods.</p>
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<p>Variation in average wave surface elevation within the chamber with different incident wave periods at various opening ratios.</p>
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<p>Variation in average pressure inside the chamber with different incident wave periods at various opening ratios.</p>
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<p>Variation in average airflow velocity at the opening orifice with different incident wave periods at various opening ratios.</p>
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<p>Variation in hydrodynamic efficiency of OWC with different incident wave periods at various opening ratios.</p>
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<p>The variation in hydrodynamic efficiency with incident wave height.</p>
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<p>Simulation model of the novel PTO system.</p>
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<p>PTO system input values: (<b>a</b>) pressure and (<b>b</b>) temperature.</p>
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<p>Simulation model of the conventional PTO system.</p>
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<p>Comparison of mass flow rate via the turbine.</p>
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<p>The pressure up- and downstream of the turbine: (<b>a</b>) novel PTO system and (<b>b</b>) conventional PTO system.</p>
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<p>Comparison of the system’s output power: (<b>a</b>) novel PTO system and (<b>b</b>) conventional PTO system.</p>
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<p>Novel PTO system for different input conditions: (<b>a</b>) mass flow rate and (<b>b</b>) output power.</p>
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20 pages, 5374 KiB  
Article
Dynamic Reaction and Damage Evaluation of Reactive Powder Concrete Strengthened Reinforced Concrete Columns Subjected to Explosive Load
by Siyuan Qiu, Jianmin Liu, Zhifu Yu, Kai Yan and Xiaomeng Hou
Buildings 2025, 15(3), 448; https://doi.org/10.3390/buildings15030448 - 31 Jan 2025
Viewed by 427
Abstract
China has an existing building area of 80 billion square meters, where reinforced concrete structures have a large quantity and a wide surface area. The risk of structures being subjected to blast loading is relatively high. Reactive powder concrete has the specialties of [...] Read more.
China has an existing building area of 80 billion square meters, where reinforced concrete structures have a large quantity and a wide surface area. The risk of structures being subjected to blast loading is relatively high. Reactive powder concrete has the specialties of ultra-high toughness, super strength, and a high strength to ponderance ratio. Reinforced concrete (RC) structures strengthened by RPC are called RPC-RC structures, which can easily elevate the explosive load resistance of building structures while also strengthening the building. It is a significant method used in avoiding the collapse of structures under explosive loads. The dynamic reaction and damage evaluation approaches of RPC-RC columns under explosive load have not been deeply studied. For addressing this issue, numerical simulation of RPC strengthened RC columns under explosive load was carried out by LS-DYNA (R10), and the correctness of the numerical simulation was verified by comparing it with relevant experimental results. In this paper, a finite element model of an RPC-RC column was established, and the main factors affecting the anti-explosion performance of an RPC-RC column were studied. The influence of the RPC reinforcement layer parameters (RPC thickness, RPC strength, longitudinal reinforcement ratio, and stirrup ratio) on the dynamic reaction and damage degree of RPC-RC columns was examined. The consequences indicated that the failure mode of the columns after RPC reinforcement can alter from bending shear damage to bending damage. As the thickness and strength of the RPC increases, the longitudinal reinforcement ratio increases, the stirrup ratio increases, and the maximum horizontal deformation of the center point of the RPC reinforced RC columns decreases. For RPC-RC columns with a height of 3–4 m and a width of 300–400 mm under blast loading, columns with an axial compression ratio greater than 0.3 will collapse, while columns with an axial compression ratio less than 0.3 are less likely to collapse. In the light of the calculation outcomes, a formula for reckoning the damage index of RPC-RC columns was proposed, taking into account factors such as proportional distance, axial compression ratio, RPC thickness, longitudinal reinforcement ratio, and stirrup ratio. Full article
(This article belongs to the Special Issue Assessment and Retrofit of Reinforced Concrete Structures)
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<p>Scale frame test model [<a href="#B18-buildings-15-00448" class="html-bibr">18</a>].</p>
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<p>RPC column geometry and steel bar layout.</p>
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<p>Finite element model of the RC and RPC columns.</p>
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<p>Mid-span deformation curve of the RC column.</p>
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<p>Mid-span deformation curve of the RPC column.</p>
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<p>Effective plastic strain diagram of the RC column.</p>
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<p>Effective plastic strain diagram of the RPC-RC column.</p>
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<p>Mid-span deformation-time history curve of the RPC and RPC-RC columns.</p>
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<p>Mid-span deformation curve of the strengthened columns with different RPC thicknesses.</p>
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<p>Maximum deformation and residual deformation with different RPC reinforcement thicknesses.</p>
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<p>Mid-span deformation curve of the strengthened columns with different RPC strengths.</p>
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<p>Maximum deformation and residual deformation with different RPC strengths.</p>
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<p>Mid-span deformation curve of the strengthened columns with different reinforcement ratios of longitudinal reinforcement.</p>
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<p>Maximum deformation and residual deformation with different reinforcement ratios of longitudinal reinforcement.</p>
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<p>Mid-span deformation curve of the strengthened columns with different stirrup ratios.</p>
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<p>Maximum deformation and residual deformation.</p>
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<p>Time-history curves of mid-span deformation with different explosive quantities and cross-sections.</p>
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<p>Relationship between explosion equivalent and damage index under different axial pressure ratios.</p>
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<p>Damage index comparison between calculated and simulated values.</p>
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28 pages, 14496 KiB  
Article
Intelligent Optimization Pathway and Impact Mechanism of Age-Friendly Neighborhood Spatial Environment Driven by NSGA-II and XGBoost
by Lu Zhang, Zizhuo Qi, Xin Yang and Ling Jiang
Appl. Sci. 2025, 15(3), 1449; https://doi.org/10.3390/app15031449 - 31 Jan 2025
Viewed by 379
Abstract
A comfortable outdoor environment, like its indoor counterpart, can significantly enhance the quality of life and improve the physical and mental health of elderly populations. Urban spatial morphology is one of the key factors influencing outdoor environmental performance. To explore the interactions between [...] Read more.
A comfortable outdoor environment, like its indoor counterpart, can significantly enhance the quality of life and improve the physical and mental health of elderly populations. Urban spatial morphology is one of the key factors influencing outdoor environmental performance. To explore the interactions between urban spatial morphology and the outdoor environment for the elderly, this study utilized parametric tools to establish a performance-driven workflow based on a “morphology generation–performance evaluation–morphology optimization” framework. Using survey data from 340 elderly neighborhoods in Beijing, a parametric urban morphology generation model was constructed. The following three optimization objectives were set: maximizing the winter pedestrian Universal Thermal Climate Index (UTCI), minimizing the summer pedestrian UTCI, and maximizing sunlight hours. Multi-objective optimization was conducted using a genetic algorithm, generating a “morphology–performance” dataset. Subsequently, the XGBoost (eXtreme Gradient Boosting) and SHAP (Shapley Additive Explanations) explainable machine learning algorithms were applied to uncover the nonlinear relationships among variables. The results indicate that optimizing spatial morphology significantly enhances environmental performance. For the summer elderly UTCI, the contributing morphological indicators include the Shape Coefficient (SC), Standard Deviation of Building Area (SA), and Deviation of Building Volume (SV), while the inhibitory indicators include the average building height (AH), Average Building Volume (AV), Mean Building Area (MA), and floor–area ratio (FAR). For the winter elderly UTCI, the contributing indicators include the AH, Volume–Area Ratio (VAR), and FAR, while the inhibitory indicators include the SC and porosity (PO). The morphological indicators contributing to sunlight hours are not clearly identified in the model, but the inhibitory indicators for sunlight hours include the AH, MA, and FAR. This study identifies the morphological indicators influencing environmental performance and provides early-stage design strategies for age-friendly neighborhood layouts, reducing the cost of later-stage environmental performance optimization. Full article
(This article belongs to the Section Applied Physics General)
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<p>Workflow of this study. (In the figure, Y/N indicates whether the generated result meets the constraints. If it is Y (yes), the generated result will proceed to the next step along the solid line. If it is N (no), the generated result will return to the previous step along the dotted line and enter a loop).</p>
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<p>Study area and distribution of survey points.</p>
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<p>Building type simplification with specific modeling parameters. (The figure shows the information of nine different types of buildings, including axonometric drawings (on the left), floor plans (on the upper right), and elevation drawings (on the lower right)).</p>
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<p>Neighborhood generation process.</p>
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<p>Visualization of morphological indicators: definitions and calculation methods.</p>
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<p>UTCI calculation flowchart. The arrows in the figure represent the simulation and calculation process of UTCI values using basic climate data.</p>
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<p>Standard deviations of objectives and average values of Pareto solution sets during the optimization process. (<b>a</b>) Standard deviation of objectives in the optimization process for UTCI-S. (<b>b</b>) Standard deviation of objectives in the optimization process for UTCI-W. (<b>c</b>) Standard deviation of objectives in the optimization process for SH. (<b>d</b>) Average values of Pareto solution sets for UTCI-S. (<b>e</b>) Average values of Pareto solution sets for UTCI-W. (<b>f</b>) Average values of Pareto solution sets for SH.</p>
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<p>Boxplots of data distribution for feasible solutions and Pareto solutions. (<b>a</b>) Data distribution for feasible solutions and Pareto solutions of UTCI-S. (<b>b</b>) Data distribution for feasible solutions and Pareto solutions of UTCI-W. (<b>c</b>) Data distribution for feasible solutions and Pareto solutions of SHs. The points in the figure represent the discrete data points in the three - group data, and the lines are the markers of the median.</p>
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<p>Three-dimensional (3D) bar charts of spatial morphology optimization results. (<b>a</b>) Data distribution of feasible solutions in the design space. (<b>b</b>) Data distribution of Pareto solutions optimized by the algorithm.</p>
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<p>Interpretability analysis of the UTCI-S model using explainable machine learning. (<b>a</b>) SHAP value bar plot. (<b>b</b>) SHAP summary plot. The black line in the figure is a reference line for a SHAP value of 0. The features corresponding to the points on the left of the line have negative SHAP values, while the features corresponding to the points on the right of the line have positive SHAP values.</p>
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<p>Interpretability analysis of the UTCI-W model using explainable machine learning. (<b>a</b>) SHAP value bar plot. (<b>b</b>) SHAP summary plot.</p>
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<p>Interpretability analysis of the SH model using explainable machine learning. (<b>a</b>) SHAP value bar plot. (<b>b</b>) SHAP summary plot.</p>
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25 pages, 10925 KiB  
Article
The Secondary Lifting Performance of Crawler Crane Under Delay Coefficient Control Strategy
by Jin Zhang, Ranheng Du, Kuo Zhang, Yin Zhang, Ying Li and Xing Chen
Machines 2025, 13(2), 106; https://doi.org/10.3390/machines13020106 - 29 Jan 2025
Viewed by 367
Abstract
Crawler cranes are mobile lifting equipment used in the process of hoisting goods. After the initial lifting, the crane may need a secondary lift due to adjustments in the position or height of the load. Addressing the common issue of load slipping during [...] Read more.
Crawler cranes are mobile lifting equipment used in the process of hoisting goods. After the initial lifting, the crane may need a secondary lift due to adjustments in the position or height of the load. Addressing the common issue of load slipping during the secondary lift caused by hydraulic motor reversal, this study proposes a control strategy applicable to crawler crane secondary lifting. Initially establishing the dynamic characteristics of the secondary lift system, incorporating a delay coefficient, and matching motor pressure build-up with memory pressure, the strategy considers a variable pump input current control to identify the relationship between motor pressure build-up and brake release. Analyzing the dynamic characteristics of secondary lifting under different conditions, this study resolves the issue of hydraulic motor reversal during the second lift caused by heavy loads. The results of this study on crawler crane secondary lifting indicate that, when using a delay coefficient of 0.70 and releasing the brake, no slip phenomenon occurred during the secondary lift process under different load conditions, categorized as 200 tons, 600 tons, and 1000 tons. This ensures the stability and transition quality of the secondary lift, providing theoretical guidance for the control of the crawler crane secondary lifting. Full article
(This article belongs to the Section Machine Design and Theory)
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<p>Schematic diagram of the 1250-ton crawler crane operation. A—Variable pump proportional valve current; P<sub>1</sub>—Motor high-pressure chamber pressure; P<sub>2</sub>—Motor low-pressure chamber pressure; P<sub>3</sub>—Brake port pressure.</p>
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<p>Transfer function block diagram of lifting hydraulic system.</p>
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<p>Secondary lifting action control strategy.</p>
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<p>Crane simulation model.</p>
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<p>Lifting system co-simulation model. 1—Electric proportional control variable pump; 2—Oil replenishment system; 3—AMESim–Simulink interface; 4—AMESim–ADAMS interface; 5—Switch valve group; 6—Brake; 7—Electric proportional control variable motor; 8—Explosion-proof valve.</p>
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<p>Input current of variable pump without control strategy.</p>
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<p>Motor speed curve without control strategy.</p>
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<p>Pressure curve of the high-pressure chamber of the motor without control strategy.</p>
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<p>Pressure curve of low-pressure chamber of the motor without control strategy.</p>
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<p>Brake-opening process.</p>
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<p>Pressure sensors at both ends of the motor.</p>
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<p>(<b>a</b>–<b>c</b>) Pressure curve of the high-pressure chamber.</p>
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<p>(<b>a</b>–<b>c</b>) Motor rotational speed curve.</p>
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<p>(<b>a</b>–<b>c</b>) Pressure curve of the low-pressure chamber.</p>
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<p>(<b>a</b>–<b>c</b>) Control strategy ahead by 70 ms.</p>
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<p>(<b>a</b>–<b>c</b>) Control strategy delay of 70 ms.</p>
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<p>Experimental test of 1250 t crawler crane.</p>
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<p>Appearance of the winch system.</p>
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<p>Variable pump sensor installation.</p>
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<p>Motor sensor installation.</p>
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<p>Electrical control system.</p>
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<p>Secondary lifting experimental curve without control strategy. (<b>a</b>) Variable pump displacement signal; (<b>b</b>) High-pressure chamber pressure of the motor; (<b>c</b>) Low-pressure chamber pressure of the motor; (<b>d</b>) Brake port pressure.</p>
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<p>The 200 t load control strategy secondary lifting experimental curve. (<b>a</b>) Variable pump displacement signal; (<b>b</b>) High-pressure chamber pressure of the motor; (<b>c</b>) Low-pressure chamber pressure of the motor; (<b>d</b>) Brake port pressure.</p>
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<p><b>The</b> 600 t load control strategy to join the control strategy of secondary lifting experimental curve. (<b>a</b>) Variable pump displacement signal; (<b>b</b>) High-pressure chamber pressure of the motor; (<b>c</b>) Low-pressure chamber pressure of the motor; (<b>d</b>) Brake port pressure.</p>
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23 pages, 9644 KiB  
Article
Modeling Urban Microclimates for High-Resolution Prediction of Land Surface Temperature Using Statistical Models and Surface Characteristics
by Md Golam Rabbani Fahad, Maryam Karimi, Rouzbeh Nazari and Mohammad Reza Nikoo
Urban Sci. 2025, 9(2), 28; https://doi.org/10.3390/urbansci9020028 - 28 Jan 2025
Viewed by 760
Abstract
Surface properties in complex urban environments can significantly impact local-level temperature gradients and distribution on several scales. Studying temperature anomalies and identifying heat pockets in urban settings is challenging. Limited high-resolution datasets are available that do not translate into an accurate assessment of [...] Read more.
Surface properties in complex urban environments can significantly impact local-level temperature gradients and distribution on several scales. Studying temperature anomalies and identifying heat pockets in urban settings is challenging. Limited high-resolution datasets are available that do not translate into an accurate assessment of near-surface temperature. This study developed a model to predict land surface temperature (LST) at a high spatial–temporal resolution in urban areas using Landsat data and meteorological inputs from NLDAS. This study developed an urban microclimate (UC) model to predict air temperature at high spatial–temporal resolution for inner urban areas through a land surface and build-up scheme. The innovative aspect of the model is the inclusion of micro-features in land use characteristics, which incorporate surface types, urban vegetation, building density and heights, short wave radiation, and relative humidity. Statistical models, including the Generalized Additive Model (GAM) and spatial autoregression (SAR), were developed to predict land surface temperature (LST) based on surface characteristics and weather parameters. The model was applied to urban microclimates in densely populated regions, focusing on Manhattan and New York City. The results indicated that the SAR model performed better (R2 = 0.85, RMSE = 0.736) in predicting micro-scale LST variations compared to the GAM (R2 = 0.39, RMSE = 1.203) and validated the accuracy of the LST prediction model with R2 ranging from 0.79 to 0.95. Full article
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<p>Administrative boundary of the borough of Manhattan in NYC and dominant land use types based on the latest National Land Cover Database (NLCD 2019).</p>
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<p>Key steps, required data processing, and methods for the proposed urban meteorological model.</p>
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<p>Snapshot of converted land surface temperature (°C) of New York City mapped within the zip codes.</p>
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<p>Comparison of downscaled NLDAS temperature with observed weather station data within three buffer zones (i.e., 1 km, 300 m, and 100 m).</p>
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<p>Results from Moran’s I index for spatial autocorrelation.</p>
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<p>GAM predicted temperature map, UC model predicted map results, and actual calculated temperature map using Landsat images.</p>
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<p>Scatter plots with R2 and RMSE values for observed vs. predicted values for the Landsat images.</p>
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13 pages, 2287 KiB  
Article
Empirical Relationships of the Characteristics of Standing Trees with the Dynamic Modulus of Elasticity of Japanese Cedar (Cryptomeria japonica) Logs: Case Study in the Kyoto Prefecture
by Kiichi Harada, Yasutaka Nakata, Masahiko Nakazawa, Keisuke Kojiro and Keiko Nagashima
Forests 2025, 16(2), 244; https://doi.org/10.3390/f16020244 - 27 Jan 2025
Viewed by 624
Abstract
With growing worldwide interest in constructing larger and taller wooden buildings, wood properties, such as the dynamic modulus of elasticity (MOEdyn), have become increasingly important. However, the MOEdyn of trees and [...] Read more.
With growing worldwide interest in constructing larger and taller wooden buildings, wood properties, such as the dynamic modulus of elasticity (MOEdyn), have become increasingly important. However, the MOEdyn of trees and logs has rarely been considered in forest management because a method for estimating the MOEdyn of logs based on standing tree characteristics has been lacking. Herein, we explored the multiple relationships between the MOEdyn of logs and standing tree characteristics of Japanese cedar (Cryptomeria japonica) such as tree height, diameter at breast height (DBH), and tree age, including the stress-wave velocity of the tree, which is known to be correlated with the MOEdyn of logs. The relationship between the MOEdyn of logs and standing tree characteristics was investigated by considering the bucking position. Different trends between the bottom logs and upper logs were found for all characteristics, showing a multiple trend of tree characteristics with the MOEdyn of logs based on the bucking position. The top three generalised linear mixed models for the prediction of the MOEdyn of logs showed relatively high accuracies when the bucking position was considered as a random effect. Although the contribution of the stress-wave velocity of the tree was relatively high, adding tree age improved the accuracy of the model, and this model was selected as the top model. The model for the bottom log, utilising the stress-wave velocity and age of the tree as explanatory variables, was highly explanatory (R2 = 0.70); however, the best model for upper logs was only moderately explanatory (R2 = 0.44). In addition, tree height and DBH were selected as explanatory variables along with tree age in the second and third models, which suggested the importance of growth rate rather than tree size. Therefore, adding correlates associated to characteristics related to height growth, such as site index, and DBH growth, such as stand density, is expected to improve model accuracy. Full article
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<p>Schematic diagram depicting the methodology used for acquiring data for the characteristics of standing trees scheduled for thinning and the cut logs of these trees after their thinning.</p>
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<p>Schematic illustration of the bucking positions and number of logs generated based on the bucking positions.</p>
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<p>Relationships between the dynamic modulus of elasticity (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> <mi>O</mi> <mi>E</mi> </mrow> <mrow> <mi>d</mi> <mi>y</mi> <mi>n</mi> </mrow> </msub> </mrow> </semantics></math>) of the cut logs and the characteristics of the standing trees from which the logs were obtained: (<b>a</b>) relationship between the <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> <mi>O</mi> <mi>E</mi> </mrow> <mrow> <mi>d</mi> <mi>y</mi> <mi>n</mi> </mrow> </msub> </mrow> </semantics></math> of logs and the stress-wave velocity of trees; (<b>b</b>) relationship between the <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> <mi>O</mi> <mi>E</mi> </mrow> <mrow> <mi>d</mi> <mi>y</mi> <mi>n</mi> </mrow> </msub> </mrow> </semantics></math> of logs and diameter at breast height; (<b>c</b>) relationship between the <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> <mi>O</mi> <mi>E</mi> </mrow> <mrow> <mi>d</mi> <mi>y</mi> <mi>n</mi> </mrow> </msub> </mrow> </semantics></math> of logs and the height of trees; and (<b>d</b>) relationship between the <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> <mi>O</mi> <mi>E</mi> </mrow> <mrow> <mi>d</mi> <mi>y</mi> <mi>n</mi> </mrow> </msub> </mrow> </semantics></math> of logs and the age of trees. The data for the bottom log are shown in blue colour and data for the upper logs are shown in grey colour.</p>
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<p>Relationships between the actual <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> <mi>O</mi> <mi>E</mi> </mrow> <mrow> <mi>d</mi> <mi>y</mi> <mi>n</mi> </mrow> </msub> </mrow> </semantics></math> of the cut logs, calculated using Equation (1), and the predicted <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> <mi>O</mi> <mi>E</mi> </mrow> <mrow> <mi>d</mi> <mi>y</mi> <mi>n</mi> </mrow> </msub> </mrow> </semantics></math> of the same logs, calculated using the developed model (Equations (4) and (5)). The data for the bottom log are shown in blue circles and data for the upper logs are shown in grey triangles.</p>
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