Nothing Special   »   [go: up one dir, main page]

You seem to have javascript disabled. Please note that many of the page functionalities won't work as expected without javascript enabled.
 
 
Sign in to use this feature.

Years

Between: -

Subjects

remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline

Journals

Article Types

Countries / Regions

remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline

Search Results (135)

Search Parameters:
Keywords = Newton type methods

Order results
Result details
Results per page
Select all
Export citation of selected articles as:
17 pages, 1206 KiB  
Article
A Smoothing Newton Method for Real-Time Pricing in Smart Grids Based on User Risk Classification
by Linsen Song and Gaoli Sheng
Mathematics 2025, 13(5), 822; https://doi.org/10.3390/math13050822 - 28 Feb 2025
Viewed by 244
Abstract
Real-time pricing is an ideal pricing mechanism for regulating the balance of power supply and demand in smart grid. Considering the differences in electricity consumption risks among different types of users, a social welfare maximization model with user risk classification is proposed in [...] Read more.
Real-time pricing is an ideal pricing mechanism for regulating the balance of power supply and demand in smart grid. Considering the differences in electricity consumption risks among different types of users, a social welfare maximization model with user risk classification is proposed in this paper. Also, a smoothing Newton method is investigated for solving the proposed model. Firstly, the convexity of the model is discussed, which implies that the local optimum of the model is also the global optimum. Then, by transforming the proposed model into a smooth equation system based on the Karush–Kuhn–Tucker (KKT) conditions, we devise a smoothing Newton algorithm integrated with Powell–Wolfe line search criteria. The nonsingularity of the corresponding function’s Jacobian matrix is obtained to ensure the stability of the proposed algorithm. Finally, we give a comparison between the proposed model and the unclassified risk model and the proposed algorithm and the distributed algorithm for real-time pricing, time-of-use pricing, and fixed pricing, respectively. The numerical results demonstrate the effectiveness of the model and the algorithm. Full article
Show Figures

Figure 1

Figure 1
<p>Comparison The flow chart of Algorithm 1.</p>
Full article ">Figure 2
<p>Comparison of price between the risk-classified model and unclassified model under different scales of users based on the smoothing Newton algorithm.</p>
Full article ">Figure 3
<p>Comparison of the social welfare between risk-classified model and unclassified model under different scales of users based on the smoothing Newton algorithm.</p>
Full article ">Figure 4
<p>Comparison of price and the social welfare between the smoothing Newton algorithm and the distributed algorithm.</p>
Full article ">Figure 5
<p>Comparison of price and the social welfare between the RTP, TOU, and FP strategies.</p>
Full article ">
20 pages, 18408 KiB  
Article
Vibration-Based Damage Prediction in Composite Concrete–Steel Structures Using Finite Elements
by Mario D. Cedeño-Rodríguez, Sergio J. Yanez, Erick I. Saavedra-Flores, Carlos Felipe Guzmán and Juan Carlos Pina
Buildings 2025, 15(2), 200; https://doi.org/10.3390/buildings15020200 - 10 Jan 2025
Viewed by 836
Abstract
The prediction of structural damage through vibrational analysis is a critical task in the field of composite structures. Structural defects and damage can negatively influence the load-carrying capacity of the beam. Therefore, detecting structural damage early is essential to preventing catastrophic failures. This [...] Read more.
The prediction of structural damage through vibrational analysis is a critical task in the field of composite structures. Structural defects and damage can negatively influence the load-carrying capacity of the beam. Therefore, detecting structural damage early is essential to preventing catastrophic failures. This study addresses the challenge of predicting damage in composite concrete–steel beams using a vibration-based finite element approach. To tackle this complex task, a finite element model to a quasi-static analysis emulating a four-point pure bending experimental test was performed. Notably, the numerical model equations were carefully modified using the Newton–Raphson method to account for the stiffness degradation resulting from material strains. These modified equations were subsequently employed in a modal analysis to compute modal shapes and natural frequencies corresponding to the stressed state. The difference between initial and damaged modal shape curvatures served as the foundation for predicting a damage index. The approach effectively captured stiffness degradation in the model, leading to observable changes in modal responses, including a reduction in natural frequencies and variations in modal shapes. This enabled the accurate prediction of damage instances during construction, service, or accidental load scenarios, thereby enhancing the structural and operational safety of composite system designs. This research contributes to the advancement of vibration-based methods for damage detection, emphasizing the complexities in characterizing damage in composite structural geometries. Further exploration and refinement of this approach are essential for the precise classification of damage types. Full article
Show Figures

Figure 1

Figure 1
<p>Scheme of the experimental four-point bending test setup [<a href="#B29-buildings-15-00200" class="html-bibr">29</a>].</p>
Full article ">Figure 2
<p>Composite concrete–steel beam FE model.</p>
Full article ">Figure 3
<p>Concrete slab finite element model.</p>
Full article ">Figure 4
<p>Modeling of the composite beam steel components. (<b>a</b>) Structural steel beam FE mesh. (<b>b</b>) Steel deck FE mesh. (<b>c</b>) Shear stud FE mesh.</p>
Full article ">Figure 5
<p>Menetrey–Willam concrete model stress-strain response.</p>
Full article ">Figure 6
<p>Boundary conditions for the FE composite beam model.</p>
Full article ">Figure 7
<p>Loading protocol.</p>
Full article ">Figure 8
<p>Load-midspan deflection curve obtained from FE simulations compared with experimental test results from Meruane et al. [<a href="#B29-buildings-15-00200" class="html-bibr">29</a>].</p>
Full article ">Figure 9
<p>Contour plots for the modal displacements.</p>
Full article ">Figure 10
<p>Natural frequency reduction percentages.</p>
Full article ">Figure 11
<p>Numerical model MSC and damage index.</p>
Full article ">Figure 12
<p>Numerical damage index.</p>
Full article ">
23 pages, 3793 KiB  
Article
Dynamics Modeling Dedicated to the Operation and Control of Underwater Vehicles
by Elżbieta Jarzębowska, Edyta Ładyżyńska-Kozdraś and Konrad Kamieniecki
Electronics 2025, 14(1), 195; https://doi.org/10.3390/electronics14010195 - 5 Jan 2025
Viewed by 636
Abstract
The paper addresses the dynamics modeling of underwater vehicles that are inertia propelled, i.e., they can move based upon the change of the amount of water in their water tanks and the motion of an internal mass, enabling maneuvers. Underwater vehicles of this [...] Read more.
The paper addresses the dynamics modeling of underwater vehicles that are inertia propelled, i.e., they can move based upon the change of the amount of water in their water tanks and the motion of an internal mass, enabling maneuvers. Underwater vehicles of this type can be successfully applied in ocean scientific reconnaissance and exploration missions or for water pollution monitoring. Usually, dynamics modeling methods for them are based upon the Newton–Euler or Lagrange approaches modified to encompass variable mass. The main motivation of this research is to explore other modeling methods and compare them to those traditionally used. In this paper, modeling methods based on the Maggi and Boltzmann–Hamel approaches are presented and discussed with respect to their effectiveness in modeling, operation, and control applications. The resulting comparisons indicate that the traditional approaches are sufficient for the analysis of vehicle operation and performance in the realization of simple tasks; however, they become of limited application when the variable mass or constraints on vehicle dynamics or motion are added or complex maneuvers are required. In this regard, the Maggi or Boltzmann–Hamel approaches are more effective for dynamics modeling. The theoretical development is illustrated by examples of vehicle dynamics developed using the approaches we propose. Full article
Show Figures

Figure 1

Figure 1
<p>Reference frames and generalized and quasi-velocities adopted to model the underwater vehicle.</p>
Full article ">Figure 2
<p>Time histories of kinematic parameters of the constant mass vehicle motion.</p>
Full article ">Figure 3
<p>Time histories of kinematic parameters of the variable mass vehicle motion.</p>
Full article ">Figure 3 Cont.
<p>Time histories of kinematic parameters of the variable mass vehicle motion.</p>
Full article ">Figure 3 Cont.
<p>Time histories of kinematic parameters of the variable mass vehicle motion.</p>
Full article ">
26 pages, 17024 KiB  
Article
Optimization on Reasonable Construction State for Cable-Stayed Bridge with Steel Box Girder Based on Multi-Objective Programming Algorithm
by Junbiao He, Wenhao Chai, Weiming Hu, Jie Dai, Jin Di and Fengjiang Qin
Appl. Sci. 2025, 15(1), 91; https://doi.org/10.3390/app15010091 - 26 Dec 2024
Viewed by 689
Abstract
The reasonable construction state of a cable-stayed bridge refers to the state achieved after construction is carried out according to a specific sequence of procedures, leading to the reasonable completion status the bridge. The corresponding construction states at each stage are considered as [...] Read more.
The reasonable construction state of a cable-stayed bridge refers to the state achieved after construction is carried out according to a specific sequence of procedures, leading to the reasonable completion status the bridge. The corresponding construction states at each stage are considered as part of the reasonable construction state. For the optimization of the construction state of cable-stayed bridges with steel box girders, a method combining a multi-objective programming algorithm with a forward iteration method is proposed to determine a reasonable construction state based on the structural characteristics and optimization principles of such bridges. First, a multi-objective programming model was established, taking the bending moments of the main girder and pylon, as well as cable forces, as objective functions. The weighted square sum method, a type of evaluation function method, was then employed to convert the multi-objective programming model into an unconstrained single-objective quadratic programming model. Subsequently, the damped Newton method was utilized to solve the quadratic programming problem. By integrating this algorithm with the forward iteration method, the reasonable construction state of a large-span and double-tower steel box girder cable-stayed bridge was optimized. The influence of different objective functions on the optimization results was analyzed. The findings demonstrate that the proposed method produces a smooth structural configuration under the optimized construction state, with internal forces and normal stresses within a reasonable range. In the completed state derived from this construction state, internal forces, normal stresses, and cable forces are uniformly distributed, while the reactions at transition piers and auxiliary piers exhibit sufficient pressure reserves. The structural state under dead load achieved through this method closely aligns with the desired reasonable completed state. Full article
(This article belongs to the Special Issue Structural Health Monitoring in Bridges and Infrastructure)
Show Figures

Figure 1

Figure 1
<p>Typical force diagram of a cable-stayed bridge.</p>
Full article ">Figure 2
<p>Iteration process of damped Newton method.</p>
Full article ">Figure 3
<p>Optimization process of constructing state for cable-stayed bridge with steel box girder.</p>
Full article ">Figure 4
<p>Layout of Xiangshan Port bridge (<b>a</b>). Dimension drawing of bridge span arrangement (<b>b</b>). Standard cross-section dimension drawings (unit: cm).</p>
Full article ">Figure 5
<p>Schematic diagram of finite element model.</p>
Full article ">Figure 6
<p>Schematic division of components.</p>
Full article ">Figure 7
<p>Influence matrix of construction cable tension on vertical displacement of main girder.</p>
Full article ">Figure 8
<p>Influence matrix of construction cable tension on horizontal displacement of pylon.</p>
Full article ">Figure 9
<p>Influence matrix of construction cable tension on bending moment of main girder.</p>
Full article ">Figure 10
<p>Influence matrix of construction cable tension on bending moment of pylon.</p>
Full article ">Figure 11
<p>Influence matrix of construction cable tension on cable force.</p>
Full article ">Figure 12
<p>Vertical displacement of main girder under unit construction cable force.</p>
Full article ">Figure 13
<p>Horizontal displacement of pylon under unit construction cable force.</p>
Full article ">Figure 14
<p>Bending moment of main girder under unit construction cable force.</p>
Full article ">Figure 15
<p>Bending moment of pylon under unit construction cable force.</p>
Full article ">Figure 16
<p>Change of objective function value along with number of iterations.</p>
Full article ">Figure 17
<p>Optimized construction tension force of stay cables.</p>
Full article ">Figure 18
<p>Vertical displacement envelope of girder during construction.</p>
Full article ">Figure 19
<p>Horizontal displacement envelope of pylon during construction.</p>
Full article ">Figure 20
<p>Axial force envelope of main girder during construction.</p>
Full article ">Figure 21
<p>Axial force envelope of pylon during construction.</p>
Full article ">Figure 22
<p>Bending moment envelope of main girder during construction.</p>
Full article ">Figure 23
<p>Bending moment envelope of pylon during construction.</p>
Full article ">Figure 24
<p>Maximum cable forces during construction.</p>
Full article ">Figure 25
<p>Minimum cable forces during construction.</p>
Full article ">Figure 26
<p>Vertical displacement of main girder under dead load.</p>
Full article ">Figure 27
<p>Horizontal displacement of pylon under dead load.</p>
Full article ">Figure 28
<p>Axial force of main girder under dead load.</p>
Full article ">Figure 29
<p>Axial force of pylon under dead load.</p>
Full article ">Figure 30
<p>Bending moment of main girder under dead load.</p>
Full article ">Figure 31
<p>Bending moment of pylon under dead load.</p>
Full article ">Figure 32
<p>Cable forces under dead load.</p>
Full article ">
23 pages, 5375 KiB  
Article
Power Flow Analysis of Ring AC/DC Hybrid Network with Multiple Power Electronic Transformers Based on Hybrid Alternating Iteration Power Flow Algorithm
by Zhen Zheng, Chenhong Huang, Xiaoli Ma, Wenwen Chen, Yinan Huang, Min Wang and Dongqian Pan
Processes 2025, 13(1), 7; https://doi.org/10.3390/pr13010007 - 24 Dec 2024
Viewed by 440
Abstract
AC/DC hybrid distribution networks with power electronic transformers (PETs) as distribution hubs are in line with the future development direction of the AC/DC hybrid distribution network. Unlike traditional transformers, power electronic transformers introduce new node types and may transform the network topology from [...] Read more.
AC/DC hybrid distribution networks with power electronic transformers (PETs) as distribution hubs are in line with the future development direction of the AC/DC hybrid distribution network. Unlike traditional transformers, power electronic transformers introduce new node types and may transform the network topology from radial to ring structures. These changes render traditional power flow calculation methods inadequate for achieving satisfactory results in AC/DC hybrid networks. In addition, existing commercial power flow calculation software packages are mainly based on the traditional AC power flow calculation method, which have limited support for the DC network. Especially when the DC network is coupled with the AC network, it is difficult to achieve a unified calculation of its power flow. To address these challenges, this paper proposes a novel power flow calculation method for ring AC/DC hybrid distribution networks with power electronic transformers. The proposed method is based on the alternating iterative method to ensure compatibility with mature AC power flow calculation programs in commercial software, thereby improving the feasibility of engineering applications. Firstly, the steady-state power flow calculation model of PET is constructed by analyzing that the working principle and control modes of power electronic transformer are proposed based on the source-load attributes of its connected subnetworks. According to the characteristics of the power electronic transformer, AC distribution network, and DC distribution network, a hybrid alternating iteration method combining the high computational accuracy of the Newton–Raphson (NR) method with the high efficiency of the Zbus Gaussian method in dealing with ring networks is proposed. On this basis, the power flow calculation model of the AC/DC hybrid distribution network with power electronic transformers is established. Finally, the simulation of the constructed 44-node ring AC/DC hybrid distribution network example is carried out. The simulation results show that the proposed method can not only converge reliably when the convergence accuracy is 1 × 10−6 p.u., but also ensure that the voltage magnitudes of all nodes are above 0.96 p.u. whose maximum offset value is 0.789% when the outputs of the connected distributed generations fluctuate, which verifies the effectiveness and accuracy of the proposed method. Full article
(This article belongs to the Section Energy Systems)
Show Figures

Figure 1

Figure 1
<p>Traditional AC distribution networks without DC bus.</p>
Full article ">Figure 2
<p>AC/DC hybrid distribution networks with non-isolated bidirectional converters.</p>
Full article ">Figure 3
<p>AC/DC hybrid distribution networks with PETs.</p>
Full article ">Figure 4
<p>Physical structure of PET.</p>
Full article ">Figure 5
<p>Model of the AC port based on VSC.</p>
Full article ">Figure 6
<p>Model of the DC port based on the DC/DC converter.</p>
Full article ">Figure 7
<p>A flowchart of the power flow calculation process for AC/DC hybrid distribution networks with PETs.</p>
Full article ">Figure 8
<p>Improved IEEE 33-bus system connected to the DC system.</p>
Full article ">Figure 9
<p>Partition results.</p>
Full article ">Figure 10
<p>Active power of all ports of two PETs.</p>
Full article ">Figure 11
<p>Voltage magnitude of all ports of two PETs.</p>
Full article ">Figure 12
<p>Modulation ratio of AC ports of two PETs.</p>
Full article ">Figure 13
<p>Outputs of PVs and WTs in three cases.</p>
Full article ">Figure 14
<p>Comparisons of the bus voltage magnitudes between three cases.</p>
Full article ">Figure 15
<p>Bus voltage offset distribution of case 2 and case 3.</p>
Full article ">Figure 16
<p>Comparisons of the active power of all ports of two PETs between three cases.</p>
Full article ">
16 pages, 777 KiB  
Article
On the Convergence of a Kurchatov-Type Method for Solving Nonlinear Equations and Its Applications
by Ioannis K. Argyros, Stepan Shakhno and Halyna Yarmola
AppliedMath 2024, 4(4), 1539-1554; https://doi.org/10.3390/appliedmath4040082 - 19 Dec 2024
Viewed by 499
Abstract
A local and a semi-local convergence analysis are presented for the Kurchatov-type method to solve numerically nonlinear equations in a Banach space. The method depends on a real parameter. By specializing the parameter, we obtain methods already studied in the literature under different [...] Read more.
A local and a semi-local convergence analysis are presented for the Kurchatov-type method to solve numerically nonlinear equations in a Banach space. The method depends on a real parameter. By specializing the parameter, we obtain methods already studied in the literature under different types of conditions, such us Newton’s, and Steffensen’s, and Kurchatov’s methods, the Secant method, and other methods. This study is carried out under generalized conditions for first-order divided differences, as well as first-order derivatives. Both in the local case and in the semi-local case, the error estimates, the radii of the region of convergence, and the regions of the solution’s uniqueness are determined. A numerical majorizing sequence is constructed for studying semi-local convergence. The approach of restricted convergence regions is used to develop a convergence analysis of the considered method. The new approach allows a comparison of the convergence of different methods under a uniform set of conditions. In particular, the assumption of generalized continuity used to control the divided difference provides more precise knowledge on the location of the solution as well as tighter error estimates. Moreover, the generality of the approach makes it useful for studying other methods in an analogous way. Numerical examples demonstrate the applicability of our theoretical results. Full article
Show Figures

Figure 1

Figure 1
<p>The concept of the investigation.</p>
Full article ">Figure 2
<p>Error for problem 2.</p>
Full article ">Figure 3
<p>Error for problem 3.</p>
Full article ">
44 pages, 7073 KiB  
Article
Integral Neuron: A New Concept for Nonlinear Neuron Modeling Using Weight Functions. Creation of XOR Neurons
by Kostadin Yotov, Emil Hadzhikolev and Stanka Hadzhikoleva
Mathematics 2024, 12(24), 3982; https://doi.org/10.3390/math12243982 - 18 Dec 2024
Viewed by 567
Abstract
In the present study, an extension of the idea of dynamic neurons is proposed by replacing the weights with a weight function that is applied simultaneously to all neuron inputs. A new type of artificial neuron called an integral neuron is modeled, in [...] Read more.
In the present study, an extension of the idea of dynamic neurons is proposed by replacing the weights with a weight function that is applied simultaneously to all neuron inputs. A new type of artificial neuron called an integral neuron is modeled, in which the total signal is obtained as the integral of the weight function. The integral neuron enhances traditional neurons by allowing the signal shape to be linear and nonlinear. The training of the integral neuron involves finding the parameters of the weight function, where its functional values directly influence the total signal in the neuron’s body. This article presents theoretical and experimental evidence for the applicability and convergence of standard training methods such as gradient descent, Gauss–Newton, and Levenberg–Marquardt in searching for the optimal weight function of an integral neuron. The experimental part of the study demonstrates that a single integral neuron can be trained on the logical XOR function—something that is impossible for single classical neurons due to the linear nature of the summation in their bodies. Full article
(This article belongs to the Section E: Applied Mathematics)
Show Figures

Figure 1

Figure 1
<p>Standalone artificial neuron.</p>
Full article ">Figure 2
<p>Neuron with dynamically changing weights for each input set.</p>
Full article ">Figure 3
<p>Rectangles with areas representing the products of inputs and their weights in a neuron.</p>
Full article ">Figure 4
<p>Example of a signal within a neuron’s body represented as the sum of areas of adjacent rectangles.</p>
Full article ">Figure 5
<p>Algorithm for finding the optimal weight function using gradient descent.</p>
Full article ">Figure 6
<p>Integral neuron equipped with smooth weight and transfer functions, <math display="inline"><semantics> <mrow> <mi mathvariant="normal">w</mi> <mfenced separators="|"> <mrow> <mi mathvariant="normal">t</mi> </mrow> </mfenced> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <mi mathvariant="normal">g</mi> </mrow> </semantics></math>, respectively.</p>
Full article ">Figure 7
<p>Algorithm for finding the optimal weight function using the Gauss–Newton method.</p>
Full article ">Figure 8
<p>Algorithm for finding the optimal weight function using the Levenberg–Marquardt method.</p>
Full article ">Figure 9
<p>Structure of an integral neuron cell.</p>
Full article ">Figure 10
<p>Integral neuron represented as a classical neuron.</p>
Full article ">Figure 11
<p>Training process for (<b>a</b>) classical neurons; (<b>b</b>) integral neurons.</p>
Full article ">Figure 12
<p>Linear separability in (<b>a</b>) logical “AND”; (<b>b</b>) logical “OR”.</p>
Full article ">Figure 13
<p>Inability to classify XOR with a single divider.</p>
Full article ">Figure 14
<p>Integral XOR neuron.</p>
Full article ">Figure 15
<p>Integral XOR neuron with transfer function <math display="inline"><semantics> <mrow> <mn>3</mn> <mi>t</mi> <mi>a</mi> <mi>h</mi> <mi>n</mi> <mo stretchy="false">(</mo> <mover accent="true"> <mrow> <mi>S</mi> </mrow> <mo stretchy="false">~</mo> </mover> <mo stretchy="false">)</mo> </mrow> </semantics></math>.</p>
Full article ">Figure 16
<p>Integral XOR neuron with transfer function <math display="inline"><semantics> <mrow> <mi>f</mi> <mfenced separators="|"> <mrow> <mi>x</mi> </mrow> </mfenced> <mo>=</mo> <mi>x</mi> </mrow> </semantics></math>.</p>
Full article ">Figure 17
<p>Integral XOR neuron with transfer function <math display="inline"><semantics> <mrow> <mi>g</mi> <mfenced separators="|"> <mrow> <mi>x</mi> </mrow> </mfenced> <mo>=</mo> <mn>2</mn> <mi>s</mi> <mi>i</mi> <mi>n</mi> <mo>(</mo> <mi>x</mi> <mo>)</mo> </mrow> </semantics></math>.</p>
Full article ">Figure 18
<p>Structure of an integral neuron with a weight function.</p>
Full article ">Figure A1
<p>MATLAB v2018a file compute_error.m—function for error calculation.</p>
Full article ">Figure A2
<p>MATLAB v2018a file Levenberg_Markvard_XOR_neuron.m—script for training the integral XOR neuron, calculating the coefficients of the weight function.</p>
Full article ">Figure A3
<p>MATLAB v2018a file Test.m—usage of the integral XOR neuron.</p>
Full article ">
17 pages, 1673 KiB  
Article
Nonlinear Thermomechanical Low-Velocity Impact Behaviors of Geometrically Imperfect GRC Beams
by Tao Zhang, Qiang Li, Jia-Jia Mao and Chunqing Zha
Materials 2024, 17(24), 6062; https://doi.org/10.3390/ma17246062 - 11 Dec 2024
Viewed by 544
Abstract
This paper studies the thermomechanical low-velocity impact behaviors of geometrically imperfect nanoplatelet-reinforced composite (GRC) beams considering the von Kármán nonlinear geometric relationship. The graphene nanoplatelets (GPLs) are assumed to have a functionally graded (FG) distribution in the matrix beam along its thickness, following [...] Read more.
This paper studies the thermomechanical low-velocity impact behaviors of geometrically imperfect nanoplatelet-reinforced composite (GRC) beams considering the von Kármán nonlinear geometric relationship. The graphene nanoplatelets (GPLs) are assumed to have a functionally graded (FG) distribution in the matrix beam along its thickness, following the X-pattern. The Halpin–Tsai model and the rule of mixture are employed to predict the effective Young modulus and other material properties. Dividing the impact process into two stages, the corresponding impact forces are calculated using the modified nonlinear Hertz contact law. The nonlinear governing equations are obtained by introducing the von Kármán nonlinear displacement–strain relationship into the first-order shear deformation theory and dispersed via the differential quadrature (DQ) method. Combining the governing equation of the impactor’s motion, they are further parametrically solved by the Newmark-β method associated with the Newton–Raphson iterative process. The influence of different types of geometrical imperfections on the nonlinear thermomechanical low-velocity impact behaviors of GRC beams with varying weight fractions of GPLs, subjected to different initial impact velocities, are studied in detail. Full article
(This article belongs to the Special Issue Functionally Graded Graphene Nanocomposite Materials and Structures)
Show Figures

Figure 1

Figure 1
<p>(<b>a</b>) <span class="html-italic">N</span>-layered geometrically imperfect GRC beam subjected to low-velocity impact and (<b>b</b>) the schematic diagram of the functionally graded distributed GPL along the thickness of the beam.</p>
Full article ">Figure 2
<p>Types of imperfection: (<b>a</b>) sine, (<b>b</b>) global, and (<b>c</b>) local.</p>
Full article ">Figure 3
<p>Comparison results: low-velocity impact force history of the intact CNTRC beam with FG-X pattern [<a href="#B52-materials-17-06062" class="html-bibr">52</a>].</p>
Full article ">Figure 4
<p>Influences of the imperfect mode and amplitude on the (<b>a</b>) time-dependent impact force and (<b>b</b>) nonlinear thermomechanical central deflection of a geometrically imperfect GRC beam.</p>
Full article ">Figure 5
<p>Effects of temperature variation on the (<b>a</b>) time-dependent impact force and (<b>b</b>) nonlinear thermomechanical central deflection of a GRC beam with different geometrical imperfections.</p>
Full article ">Figure 6
<p>Effects of the initial impact velocity of the impactor on the (<b>a</b>) time-dependent impact force and (<b>b</b>) nonlinear thermomechanical central deflection of a GRC beam with different geometrical imperfections.</p>
Full article ">Figure 7
<p>Effects of the weight fraction of GPLs and imperfect amplitude on the (<b>a</b>) time-dependent impact force and (<b>b</b>) nonlinear thermomechanical central deflection of a GRC beam with global imperfections.</p>
Full article ">Figure 8
<p>Effects of the weight fraction of GPLs and imperfect amplitude on the (<b>a</b>) time-dependent impact force and (<b>b</b>) nonlinear thermomechanical central deflection of a GRC beam with sine imperfections.</p>
Full article ">Figure 9
<p>Effects of the weight fraction of GPLs and imperfect amplitude on the (<b>a</b>) time-dependent impact force and (<b>b</b>) nonlinear thermomechanical central deflection of a GRC beam with local imperfections.</p>
Full article ">
26 pages, 5138 KiB  
Article
On Traub–Steffensen-Type Iteration Schemes With and Without Memory: Fractal Analysis Using Basins of Attraction
by Moin-ud-Din Junjua, Shahid Abdullah, Munish Kansal and Shabbir Ahmad
Fractal Fract. 2024, 8(12), 698; https://doi.org/10.3390/fractalfract8120698 - 26 Nov 2024
Viewed by 1083
Abstract
This paper investigates the design and stability of Traub–Steffensen-type iteration schemes with and without memory for solving nonlinear equations. Steffensen’s method overcomes the drawback of the derivative evaluation of Newton’s scheme, but it has, in general, smaller sets of initial guesses that converge [...] Read more.
This paper investigates the design and stability of Traub–Steffensen-type iteration schemes with and without memory for solving nonlinear equations. Steffensen’s method overcomes the drawback of the derivative evaluation of Newton’s scheme, but it has, in general, smaller sets of initial guesses that converge to the desired root. Despite this drawback of Steffensen’s method, several researchers have developed higher-order iterative methods based on Steffensen’s scheme. Traub introduced a free parameter in Steffensen’s scheme to obtain the first parametric iteration method, which provides larger basins of attraction for specific values of the parameter. In this paper, we introduce a two-step derivative free fourth-order optimal iteration scheme based on Traub’s method by employing three free parameters and a weight function. We further extend it into a two-step eighth-order iteration scheme by means of memory with the help of suitable approximations of the involved parameters using Newton’s interpolation. The convergence analysis demonstrates that the proposed iteration scheme without memory has an order of convergence of 4, while its memory-based extension achieves an order of convergence of at least 7.993, attaining the efficiency index 7.9931/32. Two special cases of the proposed iteration scheme are also presented. Notably, the proposed methods compete with any optimal j-point method without memory. We affirm the superiority of the proposed iteration schemes in terms of efficiency index, absolute error, computational order of convergence, basins of attraction, and CPU time using comparisons with several existing iterative methods of similar kinds across diverse nonlinear equations. In general, for the comparison of iterative schemes, the basins of iteration are investigated on simple polynomials of the form zn1 in the complex plane. However, we investigate the stability and regions of convergence of the proposed iteration methods in comparison with some existing methods on a variety of nonlinear equations in terms of fractals of basins of attraction. The proposed iteration schemes generate the basins of attraction in less time with simple fractals and wider regions of convergence, confirming their stability and superiority in comparison with the existing methods. Full article
Show Figures

Figure 1

Figure 1
<p>Basins of attraction of <math display="inline"><semantics> <mrow> <mi>ϕ</mi> <mrow> <mo>(</mo> <mi>z</mi> <mo>)</mo> </mrow> <mo>=</mo> <msup> <mi>z</mi> <mn>3</mn> </msup> <mo>−</mo> <mn>1</mn> </mrow> </semantics></math> using Newton’s method (<a href="#FD1-fractalfract-08-00698" class="html-disp-formula">1</a>) and Steffensen’ method (<a href="#FD2-fractalfract-08-00698" class="html-disp-formula">2</a>).</p>
Full article ">Figure 2
<p>Basins of attraction of <math display="inline"><semantics> <mrow> <mi>ϕ</mi> <mrow> <mo>(</mo> <mi>z</mi> <mo>)</mo> </mrow> <mo>=</mo> <msup> <mi>z</mi> <mn>3</mn> </msup> <mo>−</mo> <mn>1</mn> </mrow> </semantics></math> using Traub’s method (<a href="#FD3-fractalfract-08-00698" class="html-disp-formula">3</a>).</p>
Full article ">Figure 3
<p>Comparisons of various iterative methods with-memory in terms of absolute error <math display="inline"><semantics> <mrow> <mrow> <mo>|</mo> </mrow> <msub> <mi>ω</mi> <mi>j</mi> </msub> <mrow> <mo>−</mo> <mi>α</mi> <mo>|</mo> </mrow> </mrow> </semantics></math> for <math display="inline"><semantics> <mrow> <msub> <mi>ϕ</mi> <mn>1</mn> </msub> <mrow> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> <mo>−</mo> <msub> <mi>ϕ</mi> <mn>7</mn> </msub> <mrow> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> in first three iterations.</p>
Full article ">Figure 3 Cont.
<p>Comparisons of various iterative methods with-memory in terms of absolute error <math display="inline"><semantics> <mrow> <mrow> <mo>|</mo> </mrow> <msub> <mi>ω</mi> <mi>j</mi> </msub> <mrow> <mo>−</mo> <mi>α</mi> <mo>|</mo> </mrow> </mrow> </semantics></math> for <math display="inline"><semantics> <mrow> <msub> <mi>ϕ</mi> <mn>1</mn> </msub> <mrow> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> <mo>−</mo> <msub> <mi>ϕ</mi> <mn>7</mn> </msub> <mrow> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> in first three iterations.</p>
Full article ">Figure 4
<p>Comparisons of various iterative methods with-memory in terms of COC, EI, and CPU time for <math display="inline"><semantics> <mrow> <msub> <mi>ϕ</mi> <mn>1</mn> </msub> <mrow> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> <mo>−</mo> <msub> <mi>ϕ</mi> <mn>7</mn> </msub> <mrow> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> respectively.</p>
Full article ">Figure 4 Cont.
<p>Comparisons of various iterative methods with-memory in terms of COC, EI, and CPU time for <math display="inline"><semantics> <mrow> <msub> <mi>ϕ</mi> <mn>1</mn> </msub> <mrow> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> <mo>−</mo> <msub> <mi>ϕ</mi> <mn>7</mn> </msub> <mrow> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> respectively.</p>
Full article ">Figure 5
<p>Basins of attraction of <math display="inline"><semantics> <mrow> <msub> <mi>ϕ</mi> <mn>1</mn> </msub> <mrow> <mo>(</mo> <mi>z</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> using several iteration methods without memory.</p>
Full article ">Figure 6
<p>Basins of attraction of <math display="inline"><semantics> <mrow> <msub> <mi>ϕ</mi> <mn>2</mn> </msub> <mrow> <mo>(</mo> <mi>z</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> using several iteration methods without memory.</p>
Full article ">Figure 7
<p>Basins of attraction of <math display="inline"><semantics> <mrow> <msub> <mi>ϕ</mi> <mn>3</mn> </msub> <mrow> <mo>(</mo> <mi>z</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> using several iteration methods without memory.</p>
Full article ">Figure 8
<p>Basins of attraction of <math display="inline"><semantics> <mrow> <msub> <mi>ϕ</mi> <mn>4</mn> </msub> <mrow> <mo>(</mo> <mi>z</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> using several iteration methods without memory.</p>
Full article ">Figure 9
<p>Basins of attraction of <math display="inline"><semantics> <mrow> <msub> <mi>ϕ</mi> <mn>5</mn> </msub> <mrow> <mo>(</mo> <mi>z</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> using several iteration methods without memory.</p>
Full article ">Figure 10
<p>Basins of attraction of <math display="inline"><semantics> <mrow> <msub> <mi>ϕ</mi> <mn>6</mn> </msub> <mrow> <mo>(</mo> <mi>z</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> using several iteration methods without memory.</p>
Full article ">Figure 11
<p>Basins of attraction of <math display="inline"><semantics> <mrow> <msub> <mi>ϕ</mi> <mn>7</mn> </msub> <mrow> <mo>(</mo> <mi>z</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> using several iteration methods without memory.</p>
Full article ">
29 pages, 5815 KiB  
Article
Grey-Box Energy Modelling of Energy-Efficient House Using Hybrid Optimization Technique of Genetic Algorithms (GA) and Quasi-Newton Algorithms with Markov Chain Monte Carlo Uncertainty Distribution
by Gulsun Demirezen, Alan S. Fung and Aidan Brookson
Energies 2024, 17(23), 5941; https://doi.org/10.3390/en17235941 - 26 Nov 2024
Viewed by 542
Abstract
Understanding energy demands and costs is important for policy makers and the energy sector, especially in the context of residential heating and cooling systems. To estimate the thermal demand of a residential house, a grey-box modelling method with a resistance–capacitance (RC) analogy was [...] Read more.
Understanding energy demands and costs is important for policy makers and the energy sector, especially in the context of residential heating and cooling systems. To estimate the thermal demand of a residential house, a grey-box modelling method with a resistance–capacitance (RC) analogy was implemented. The architectural properties used to parameterize the grey-box model were derived from a house used for research purposes in Vaughan, Ontario, Canada (TRCA-House A). The house model accounts for solar irradiance on exterior building surfaces, thermal conductivity through all surfaces, solar heat gains through windows, and thermal gains from ventilation. Two parallel short- and long-term calibrations were performed such that model outputs reflected the real-world operation of the house as best as possible. To define the unknown model parameters (such as the conductivity of building materials and some constant parameters), a hybrid optimization scheme including a genetic algorithm (GA) and the Quasi-Newton algorithm was introduced and implemented using Bayesian approximation and Markov Chain Monte Carlo (MCMC) methods. The temperature outputs from the model were compared to the data retrieved from TRCA-House A. The final iteration of the model had an RMSE for interior zone temperature estimation of 0.22 °C when compared to the retrieved interior zone temperature data from TRCA-House A. Furthermore, the annual heating and cooling energy consumption values are within 1.50% and 0.08% of target values, respectively. According to these preliminary results, the introduced model and optimization techniques could be adjusted for different types of housing, as well as for smart control applications on both a short- and long-term basis. Full article
(This article belongs to the Section G: Energy and Buildings)
Show Figures

Figure 1

Figure 1
<p>The Archetype Sustainable Houses at the Living City Campus.</p>
Full article ">Figure 2
<p>Data Management System hierarchy [<a href="#B36-energies-17-05941" class="html-bibr">36</a>].</p>
Full article ">Figure 3
<p>Relevant solar calculation angles [<a href="#B39-energies-17-05941" class="html-bibr">39</a>].</p>
Full article ">Figure 4
<p>Window heat flow diagram.</p>
Full article ">Figure 5
<p>The three-layer wall heat flow diagram.</p>
Full article ">Figure 6
<p>Simplified three-layer wall heat flow diagram.</p>
Full article ">Figure 7
<p>ASHRAE summer and winter thermal comfort zones [<a href="#B48-energies-17-05941" class="html-bibr">48</a>].</p>
Full article ">Figure 8
<p>House A mechanical system power consumption.</p>
Full article ">Figure 9
<p>Heat recovery ventilator ANN performance.</p>
Full article ">Figure 10
<p>Ambient conditions over cool-down test period.</p>
Full article ">Figure 11
<p>Parameter estimation using the Bayesian approach for the unknown parameters. Shaded (blue) areas are 90% credibility intervals. After obtaining the credibility intervals updated through MCMC analysis, the calibrated values from three-layer modelling are obtained. The credibility intervals are plotted in <a href="#energies-17-05941-f012" class="html-fig">Figure 12</a>. All the calibrated parameters are within possible ranges for real-world building materials. Since these parameters produce a model that accurately simulates the operation of the ASH-A, they have been used for all building simulations in the remainder of this work.</p>
Full article ">Figure 12
<p>Credibility intervals found through MCMC analysis. The orange lines stand for the credibility intervals found through Bayesian methodology; the blue lines stand for the updated credibility intervals.</p>
Full article ">Figure 13
<p>Short-term calibration performance.</p>
Full article ">Figure 14
<p>Annual hourly simulated heating and cooling energy output.</p>
Full article ">
25 pages, 7192 KiB  
Article
Quaternion-Based Non-Singular Terminal Sliding Mode Control of Quadrotor with a Two-Degree-of-Freedom Deformable Arm for Narrow Environments
by Luwei Liao, Zhong Yang, Xu Chen, Haoze Zhuo, Hongyu Xu, Nuo Xu and Danguo Cheng
Drones 2024, 8(11), 629; https://doi.org/10.3390/drones8110629 - 31 Oct 2024
Viewed by 827
Abstract
Conventional multi-rotors with limited deformation capability are unable to meet the traversal capability of complex and narrow environments. In order to solve the above problems, a novel type of deformable quadrotor with a two-degree-of-freedom arm, named QTDA, is proposed. Firstly, the overall structural [...] Read more.
Conventional multi-rotors with limited deformation capability are unable to meet the traversal capability of complex and narrow environments. In order to solve the above problems, a novel type of deformable quadrotor with a two-degree-of-freedom arm, named QTDA, is proposed. Firstly, the overall structural design of the QTDA is introduced, and its movement strategy is analyzed. Secondly, the Newton–Euler equations based on a quaternion are utilized to model the omnidirectional dynamics and kinematics of the system. Next, to tackle the multi-actuator control problem, a pseudo-inverse control allocation method is developed, along with an analysis of control allocation singularities. Furthermore, non-singular terminal sliding mode position control law and non-singular terminal sliding mode attitude control law based on a quaternion are designed. Finally, simulations are conducted to verify the effectiveness of the proposed control methods. The results demonstrate the QTDA’s ability to traverse both narrow horizontal and vertical environments, thereby validating the effectiveness of the approach presented in this paper. Full article
Show Figures

Figure 1

Figure 1
<p>Multi-rotors in different complex and narrow environments. (<b>a</b>) Multi-rotors in pipeline environments. (<b>b</b>) Multi-rotors in jungle environments.</p>
Full article ">Figure 2
<p>Different deformable multi-rotors. (<b>a</b>) Falanga’s [<a href="#B4-drones-08-00629" class="html-bibr">4</a>] multi-rotor. (<b>b</b>) Riviere’s [<a href="#B5-drones-08-00629" class="html-bibr">5</a>] multi-rotor. (<b>c</b>) Zhao’s [<a href="#B6-drones-08-00629" class="html-bibr">6</a>] multi-rotor. (<b>d</b>) Kamel’s [<a href="#B8-drones-08-00629" class="html-bibr">8</a>] multi-rotor. (<b>e</b>) Brescianini’s [<a href="#B9-drones-08-00629" class="html-bibr">9</a>] multi-rotor. (<b>f</b>) Li’s [<a href="#B10-drones-08-00629" class="html-bibr">10</a>] multi-rotor.</p>
Full article ">Figure 3
<p>The structure of the QTDA and the QTDA’s arm. (<b>a</b>) The structure of the QTDA. (<b>b</b>) The QTDA’s arm.</p>
Full article ">Figure 4
<p>QTDA traverses horizontal and vertical complex and narrow environment. (<b>a</b>) QTDA traverses horizontal complex and narrow environment. (<b>b</b>) QTDA traverses vertical complex and narrow environment.</p>
Full article ">Figure 5
<p>XY-axis singularity deformation flight of QTDA. (<b>a</b>) X-axis singularity deformation flight of QTDA. (<b>b</b>) Y-axis singularity deformation flight of QTDA.</p>
Full article ">Figure 6
<p>The whole control system framework of QTDA.</p>
Full article ">Figure 7
<p>Quaternion curves in omnidirectional attitude simulation. (<b>a</b>) <math display="inline"><semantics> <msub> <mi>q</mi> <mn>0</mn> </msub> </semantics></math> of quaternion curves in omnidirectional attitude simulation. (<b>b</b>) <math display="inline"><semantics> <msub> <mi>q</mi> <mn>1</mn> </msub> </semantics></math> of quaternion curves in omnidirectional attitude simulation. (<b>c</b>) <math display="inline"><semantics> <msub> <mi>q</mi> <mn>2</mn> </msub> </semantics></math> of quaternion curves in omnidirectional attitude simulation. (<b>d</b>) <math display="inline"><semantics> <msub> <mi>q</mi> <mn>3</mn> </msub> </semantics></math> of quaternion curves in omnidirectional attitude simulation.</p>
Full article ">Figure 8
<p>Euler angle curves in omnidirectional attitude simulation. (<b>a</b>) Roll angle curve in omnidirectional attitude simulation. (<b>b</b>) Pitch angle curve in omnidirectional attitude simulation. (<b>c</b>) Yaw angle curve in omnidirectional attitude simulation.</p>
Full article ">Figure 9
<p>Motor <math display="inline"><semantics> <msub> <mi>n</mi> <mi>i</mi> </msub> </semantics></math> curves in attitude simulation. (<b>a</b>) <math display="inline"><semantics> <msub> <mi>n</mi> <mn>1</mn> </msub> </semantics></math> curve in attitude simulation. (<b>b</b>) <math display="inline"><semantics> <msub> <mi>n</mi> <mn>2</mn> </msub> </semantics></math> curve in attitude simulation. (<b>c</b>) <math display="inline"><semantics> <msub> <mi>n</mi> <mn>3</mn> </msub> </semantics></math> curve in attitude simulation. (<b>d</b>) <math display="inline"><semantics> <msub> <mi>n</mi> <mn>4</mn> </msub> </semantics></math> curve in attitude simulation.</p>
Full article ">Figure 10
<p>Servo <math display="inline"><semantics> <msub> <mi>γ</mi> <mi>i</mi> </msub> </semantics></math> curves in attitude simulation. (<b>a</b>) <math display="inline"><semantics> <msub> <mi>γ</mi> <mn>1</mn> </msub> </semantics></math> curve in attitude simulation. (<b>b</b>) <math display="inline"><semantics> <msub> <mi>γ</mi> <mn>2</mn> </msub> </semantics></math> curve in attitude simulation. (<b>c</b>) <math display="inline"><semantics> <msub> <mi>γ</mi> <mn>3</mn> </msub> </semantics></math> curve in attitude simulation. (<b>d</b>) <math display="inline"><semantics> <msub> <mi>γ</mi> <mn>4</mn> </msub> </semantics></math> curve in attitude simulation.</p>
Full article ">Figure 11
<p>Three−dimensional position simulation curve of QTDA.</p>
Full article ">Figure 12
<p>Position simulation curves of QTDA. (<b>a</b>) X−axis curve in position simulation of QTDA. (<b>b</b>) Y−axis curve in position simulation of QTDA. (<b>c</b>) Z−axis curve in position simulation of QTDA.</p>
Full article ">Figure 13
<p>Position simulation curves of QTDA in disturbance simulation. (<b>a</b>) X−axis simulation curves of QTDA in disturbance simulation. (<b>b</b>) Y−axis simulation curves of QTDA in disturbance simulation. (<b>c</b>) Z−axis simulation curves of QTDA in disturbance simulation.</p>
Full article ">Figure 14
<p>Quaternion curves in disturbance simulation. (<b>a</b>) <math display="inline"><semantics> <msub> <mi>q</mi> <mn>0</mn> </msub> </semantics></math> of quaternion curves in disturbance simulation. (<b>b</b>) <math display="inline"><semantics> <msub> <mi>q</mi> <mn>1</mn> </msub> </semantics></math> of quaternion curves in disturbance simulation. (<b>c</b>) <math display="inline"><semantics> <msub> <mi>q</mi> <mn>2</mn> </msub> </semantics></math> of quaternion curves in disturbance simulation. (<b>d</b>) <math display="inline"><semantics> <msub> <mi>q</mi> <mn>3</mn> </msub> </semantics></math> of quaternion curves in disturbance simulation.</p>
Full article ">Figure 15
<p>Euler angle curves in disturbance simulation. (<b>a</b>) Roll curve in disturbance simulation. (<b>b</b>) Pitch curve in disturbance simulation. (<b>c</b>) Yaw curve in disturbance simulation.</p>
Full article ">Figure 16
<p>Different deformations simulation at <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <msup> <mn>90</mn> <mo>∘</mo> </msup> </mrow> </semantics></math>. (<b>a</b>) <math display="inline"><semantics> <msub> <mi>β</mi> <mi>i</mi> </msub> </semantics></math> curve at <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <msup> <mn>90</mn> <mo>∘</mo> </msup> </mrow> </semantics></math>. (<b>b</b>) Quaternion curve at <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <msup> <mn>90</mn> <mo>∘</mo> </msup> </mrow> </semantics></math>. (<b>c</b>) Motor <math display="inline"><semantics> <msub> <mi>n</mi> <mi>i</mi> </msub> </semantics></math> curve at <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <msup> <mn>90</mn> <mo>∘</mo> </msup> </mrow> </semantics></math>. (<b>d</b>) Servo <math display="inline"><semantics> <msub> <mi>γ</mi> <mi>i</mi> </msub> </semantics></math> curve at <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <msup> <mn>90</mn> <mo>∘</mo> </msup> </mrow> </semantics></math>.</p>
Full article ">Figure 17
<p>Different deformations simulation at <math display="inline"><semantics> <mrow> <mi>ϕ</mi> <mo>=</mo> <msup> <mn>90</mn> <mo>∘</mo> </msup> </mrow> </semantics></math>. (<b>a</b>) <math display="inline"><semantics> <msub> <mi>β</mi> <mi>i</mi> </msub> </semantics></math> curve at <math display="inline"><semantics> <mrow> <mi>ϕ</mi> <mo>=</mo> <msup> <mn>90</mn> <mo>∘</mo> </msup> </mrow> </semantics></math>. (<b>b</b>) Quaternion curve at <math display="inline"><semantics> <mrow> <mi>ϕ</mi> <mo>=</mo> <msup> <mn>90</mn> <mo>∘</mo> </msup> </mrow> </semantics></math>. (<b>c</b>) Motor <math display="inline"><semantics> <msub> <mi>n</mi> <mi>i</mi> </msub> </semantics></math> curve at <math display="inline"><semantics> <mrow> <mi>ϕ</mi> <mo>=</mo> <msup> <mn>90</mn> <mo>∘</mo> </msup> </mrow> </semantics></math>. (<b>d</b>) Servo <math display="inline"><semantics> <msub> <mi>γ</mi> <mi>i</mi> </msub> </semantics></math> curve at <math display="inline"><semantics> <mrow> <mi>ϕ</mi> <mo>=</mo> <msup> <mn>90</mn> <mo>∘</mo> </msup> </mrow> </semantics></math>.</p>
Full article ">Figure 18
<p>Three−dimensional curve of XY−axis deformation in horizontal narrow environment. (a) First step in horizontal narrow environment. (b) Second step in horizontal narrow environment. (c) Third step in horizontal narrow environment. (d) Fourth step in horizontal narrow environment.</p>
Full article ">Figure 19
<p>Deformation simulation in horizontal narrow environment. (<b>a</b>) <math display="inline"><semantics> <msub> <mi>β</mi> <mi>i</mi> </msub> </semantics></math> curves at deformation simulation in horizontal narrow environment. (<b>b</b>) Quaternion curves at deformation simulation in horizontal narrow environment. (<b>c</b>) Euler angle curves at deformation simulation in horizontal narrow environment. (<b>d</b>) Position curves at deformation simulation in horizontal narrow environment.</p>
Full article ">Figure 20
<p>Three−dimensional curve of XY-axis deformation in vertical narrow environment. (a) First step in vertical narrow environment. (b) Second step in vertical narrow environment. (c) Third step in vertical narrow environment. (d) Fourth step in vertical narrow environment. (e) Fifth step in vertical narrow environment. (f) Sixth step in vertical narrow environment.</p>
Full article ">Figure 21
<p>Deformation simulation in vertical narrow environment. (<b>a</b>) <math display="inline"><semantics> <msub> <mi>β</mi> <mi>i</mi> </msub> </semantics></math> curves at deformation simulation in vertical narrow environment. (<b>b</b>) Quaternion curves at deformation simulation in vertical narrow environment. (<b>c</b>) Euler angle curves at deformation simulation in vertical narrow environment. (<b>d</b>) Position curves at deformation simulation in vertical narrow environment.</p>
Full article ">
22 pages, 1273 KiB  
Article
Estimation of Lifetime Performance Index for Generalized Inverse Lindley Distribution Under Adaptive Progressive Type-II Censored Lifetime Test
by Shixiao Xiao, Xue Hu and Haiping Ren
Axioms 2024, 13(10), 727; https://doi.org/10.3390/axioms13100727 - 18 Oct 2024
Cited by 1 | Viewed by 852
Abstract
The lifetime performance index (LPI) is an important metric for evaluating product quality, and research on the statistical inference of the LPI is of great significance. This paper discusses both the classical and Bayesian estimations of the LPI under an adaptive progressive type-II [...] Read more.
The lifetime performance index (LPI) is an important metric for evaluating product quality, and research on the statistical inference of the LPI is of great significance. This paper discusses both the classical and Bayesian estimations of the LPI under an adaptive progressive type-II censored lifetime test, assuming that the product’s lifetime follows a generalized inverse Lindley distribution. At first, the maximum likelihood estimator of the LPI is derived, and the Newton–Raphson iterative method is adopted to solve the numerical solution due to the log-likelihood equations having no analytical solutions. If the exact distribution of the LPI is not available, then the asymptotic confidence interval and bootstrap confidence interval of the LPI are constructed. For the Bayesian estimation, the Bayesian estimators of the LPI are derived under three different loss functions. Due to the complex multiple integrals involved in these estimators, the MCMC method is used to draw samples and further construct the HPD credible interval of the LPI. Finally, Monte Carlo simulations are used to observe the performance of these estimators in terms of the average bias and mean squared error, and two practical examples are used to illustrate the application of the proposed estimation method. Full article
Show Figures

Figure 1

Figure 1
<p>Schematic representation of the adaptive progressive type-II censored test.</p>
Full article ">Figure 2
<p>(<b>a</b>) The diagram of the PDF. (<b>b</b>) The diagram of the HF.</p>
Full article ">Figure 3
<p>(<b>a</b>) Fitting of GILD on duration of remission. (<b>b</b>) Fitting of GILD on failure time.</p>
Full article ">Figure 4
<p>The partial derivatives of the log-likelihood function.</p>
Full article ">
17 pages, 4487 KiB  
Article
Multi-Body Dynamics Modeling and Simulation of Maglev Satellites
by Zongyu Li, Weijie Wang and Lifen Wang
Appl. Sci. 2024, 14(17), 7588; https://doi.org/10.3390/app14177588 - 28 Aug 2024
Viewed by 1069
Abstract
The Lorentz force magnetic levitation gim2bal stabilized platform (LFMP), as a new generation of high-precision turntable for maglev satellites, can meet the requirements of future spacecraft for ultra-high attitude pointing accuracy and stability. To solve the problem of three-module multi-body attitude control under [...] Read more.
The Lorentz force magnetic levitation gim2bal stabilized platform (LFMP), as a new generation of high-precision turntable for maglev satellites, can meet the requirements of future spacecraft for ultra-high attitude pointing accuracy and stability. To solve the problem of three-module multi-body attitude control under maneuvering conditions, the platform subsystem is first dynamically modeled based on the second type of Lagrangian equation, and the payload subsystem is dynamically modeled based on the Newton–Euler method. Secondly, a multi-loop control system is designed, consisting of high-precision and fast attitude pointing control for the payload, position tracking control for the platform subsystem, and tracking control for the maglev module. The final simulation results verified the feasibility and effectiveness of the payload-centered control method. An evaluation of the stability with a specific model has been performed, and the attitude accuracy of the payload is within 0.00002° and the attitude stability is within 0.00005°/s. Full article
Show Figures

Figure 1

Figure 1
<p>Structure diagram of maglev satellite.</p>
Full article ">Figure 2
<p>A multi-body dynamic modeling scheme for LMFPs.</p>
Full article ">Figure 3
<p>Coordinate system definition diagram.</p>
Full article ">Figure 4
<p>Position vector definition diagram.</p>
Full article ">Figure 5
<p>Three-body High-precision attitude control scheme centered on payload.</p>
Full article ">Figure 6
<p>Control expectations. (<b>a</b>) Expected angle; (<b>b</b>) expected angular velocity; (<b>c</b>) expected angular acceleration.</p>
Full article ">Figure 6 Cont.
<p>Control expectations. (<b>a</b>) Expected angle; (<b>b</b>) expected angular velocity; (<b>c</b>) expected angular acceleration.</p>
Full article ">Figure 7
<p>Attitude accuracy of payload subsystem.</p>
Full article ">Figure 8
<p>Attitude stability of payload subsystem.</p>
Full article ">Figure 9
<p>Platform subsystem position control accuracy.</p>
Full article ">Figure 10
<p>Error in driving control of MM.</p>
Full article ">
20 pages, 351 KiB  
Article
Finite Element Method for a Fractional-Order Filtration Equation with a Transient Filtration Law
by Nurlana Alimbekova, Abdumauvlen Berdyshev, Muratkan Madiyarov and Yerlan Yergaliyev
Mathematics 2024, 12(16), 2519; https://doi.org/10.3390/math12162519 - 15 Aug 2024
Viewed by 959
Abstract
In this article, a numerical method is proposed and investigated for an initial boundary value problem governed by a fractional differential generalization of the nonlinear transient filtration law which describes fluid motion in a porous medium. This type of equation is widely used [...] Read more.
In this article, a numerical method is proposed and investigated for an initial boundary value problem governed by a fractional differential generalization of the nonlinear transient filtration law which describes fluid motion in a porous medium. This type of equation is widely used to describe complex filtration processes such as fluid movement in horizontal wells in fractured geological formations. To construct the numerical method, a high-order approximation formula for the fractional derivative in the sense of Caputo is applied, and a combination of the finite difference method with the finite element method is used. The article proves the uniqueness and continuous dependence of the solution on the input data in differential form, as well as the stability and convergence of the proposed numerical scheme. The linearization of nonlinear terms is carried out by the Newton method, which allows for achieving high accuracy in solving complex problems. The research results are confirmed by a series of numerical tests that demonstrate the applicability of the developed method in real engineering problems. The practical significance of the presented approach lies in its ability to accurately and effectively model filtration processes in shale formations, which allows engineers and geologists to make more informed decisions when designing and operating oil fields. Full article
Show Figures

Figure 1

Figure 1
<p>Error plots obtained for different orders of fractional derivatives.</p>
Full article ">
19 pages, 7143 KiB  
Article
Theoretical Evaluation of Lubrication Performance of Thrust-Type Foil Bearings in Liquid Nitrogen
by Hang Dou, Tao Jiang, Longgui He, Shuo Cheng, Xiaoliang Fang and Jimin Xu
Lubricants 2024, 12(7), 257; https://doi.org/10.3390/lubricants12070257 - 17 Jul 2024
Viewed by 918
Abstract
The development of reusable liquid rocket turbopumps has gradually highlighted the disadvantages of rolling bearings, particularly the contradiction between long service life and high rotational speed. It is critical to explore a feasible bearing scheme offering a long wear life and high stability [...] Read more.
The development of reusable liquid rocket turbopumps has gradually highlighted the disadvantages of rolling bearings, particularly the contradiction between long service life and high rotational speed. It is critical to explore a feasible bearing scheme offering a long wear life and high stability to replace the existing rolling bearings. In this study, liquid nitrogen is adopted to simulate the ultra-low temperature environment of liquid rocket turbopumps, and theoretical evaluations of the lubrication performance of thrust-type foil bearings in liquid nitrogen are conducted. A link-spring model for the bump foil structure and a thin-plate finite element model for the top foil structure are established. The static and dynamic characteristics of the bearings are analyzed using methods including the finite difference method, the Newton–Raphson iteration method, and the finite element method. Detailed analysis includes the effects of factors such as rotational speed, fluid film thickness, thrust disk tilt angle, and the friction coefficient of the bump foil interface on the static and dynamic characteristics of thrust-type foil bearings. The research results indicate that thrust-type foil bearings have a good load-carrying capacity and low frictional power consumption. The adaptive deformation of the foil structure increases the fluid film thickness, preventing dry friction due to direct contact between the rotor journal and the bearing surface. When faced with thrust disk tilt, the direct translational stiffness and damping coefficient of the bearing do not undergo significant changes, ensuring system stability. Based on the results of this study, the exceptional performance characteristics of thrust-type foil bearings make them a promising alternative to rolling bearings for the development of reusable liquid rocket turbopumps. Full article
(This article belongs to the Special Issue Aerospace Tribology)
Show Figures

Figure 1

Figure 1
<p>(<b>a</b>) Structural diagram of the thrust-type foil bearing, and (<b>b</b>) schematic diagram of the fluid film.</p>
Full article ">Figure 2
<p>Coordinate system of thrust-type bearing considering rotor misalignment.</p>
Full article ">Figure 3
<p>Link-spring model of bump foils.</p>
Full article ">Figure 4
<p>Flow diagram for calculating the static and dynamic characteristics of thrust-type foil bearings.</p>
Full article ">Figure 5
<p>Comparison between theoretical calculation results using analysis method developed in this study and experimental results in Dickman, 2010 [<a href="#B37-lubricants-12-00257" class="html-bibr">37</a>].</p>
Full article ">Figure 6
<p>Effect of (<b>a</b>) friction coefficient and (<b>b</b>) rotational speed on bump foil stiffness (<span class="html-italic">N</span> = 5, <span class="html-italic">h</span><sub>2</sub> = 10 μm).</p>
Full article ">Figure 7
<p>Distributions of (<b>a</b>) fluid film pressure and (<b>b</b>) foil deformation with thrust disk inclined at <math display="inline"><semantics> <mrow> <msub> <mi>φ</mi> <mi>x</mi> </msub> </mrow> </semantics></math> = 0.004° (speed = 2.5 × 10<sup>4</sup> r·min<sup>−1</sup>, <span class="html-italic">N</span> = 5, <span class="html-italic">h</span><sub>2</sub> = 10 μm, <span class="html-italic">μ</span> = 0.1, <span class="html-italic">η</span> = 0.1).</p>
Full article ">Figure 8
<p>Impact of friction coefficient on (<b>a</b>) static load and (<b>b</b>) friction torque of thrust pads (<span class="html-italic">N</span> = 5, <span class="html-italic">h</span><sub>2</sub> = 10 μm, <span class="html-italic">η</span> = 0.1).</p>
Full article ">Figure 9
<p>Impact of minimum initial fluid film thickness on (<b>a</b>) static load and (<b>b</b>) friction torque of thrust pads (<span class="html-italic">h<sub>t</sub></span> = 26 μm, <span class="html-italic">μ</span> = 0.1, <span class="html-italic">η</span> = 0.1).</p>
Full article ">Figure 10
<p>Impact of wedge height on (<b>a</b>) static load and (<b>b</b>) friction torque of thrust pads (<span class="html-italic">h</span><sub>2</sub> = 10 μm, <span class="html-italic">μ</span> = 0.1, <span class="html-italic">η</span> = 0.1).</p>
Full article ">Figure 11
<p>Impact of thrust disk inclination angle on (<b>a</b>) static load and (<b>b</b>) friction torque of thrust pads (speed = 2.5 × 10<sup>4</sup> r·min<sup>−1</sup>, <span class="html-italic">N</span> = 5, <span class="html-italic">h<sub>2</sub></span> = 10 μm, <span class="html-italic">μ</span> = 0.1, <span class="html-italic">η</span> = 0.1).</p>
Full article ">Figure 12
<p>Impact of thrust disk inclination angle on (<b>a</b>) static load and (<b>b</b>) friction torque of thrust-type foil bearings (speed = 2.5 × 10<sup>4</sup> r·min<sup>−1</sup>, <span class="html-italic">N</span> = 5, <span class="html-italic">h</span><sub>2</sub> = 10 μm, <span class="html-italic">μ</span> = 0.1, <span class="html-italic">η</span> = 0.1).</p>
Full article ">Figure 13
<p>Effect of excitation frequency ratio on (<b>a</b>) direct translational stiffness and (<b>b</b>) damping coefficients of thrust pads (<span class="html-italic">N</span> = 5, <span class="html-italic">h</span><sub>2</sub> = 10 μm, <span class="html-italic">μ</span> = 0.1, <span class="html-italic">η</span> = 0.1).</p>
Full article ">Figure 14
<p>Effect of friction coefficient on (<b>a</b>) direct translational stiffness and (<b>b</b>) damping coefficients of thrust pads (<span class="html-italic">N</span> = 5, <span class="html-italic">h</span><sub>2</sub> = 10 μm, <span class="html-italic">μ</span> = 0.1, <span class="html-italic">η</span> = 0.1).</p>
Full article ">Figure 15
<p>Effect of minimum initial fluid film thickness on (<b>a</b>) direct translational stiffness and (<b>b</b>) damping coefficients of thrust pads (<span class="html-italic">h<sub>t</sub></span> = 26 μm, <span class="html-italic">μ</span> = 0.1, <span class="html-italic">η</span> = 0.1).</p>
Full article ">Figure 16
<p>Effect of wedge height on (<b>a</b>) direct translational stiffness and (<b>b</b>) damping coefficients of thrust pads (<span class="html-italic">h</span><sub>2</sub> = 10 μm, <span class="html-italic">μ</span> = 0.1, <span class="html-italic">η</span> = 0.1).</p>
Full article ">Figure 17
<p>Effect of thrust disk inclination angle on the dynamic stiffness and dynamic damping coefficients of thrust-type foil bearings (speed = 2.5 × 10<sup>4</sup> r·min<sup>−1</sup>, <span class="html-italic">N</span> = 5, <span class="html-italic">h</span><sub>2</sub> = 10 μm, <span class="html-italic">μ</span> = 0.1, <span class="html-italic">η</span> = 0.1): (<b>a</b>,<b>b</b>) dynamic stiffness coefficients; (<b>c</b>,<b>d</b>) dynamic damping coefficients.</p>
Full article ">Figure 18
<p>Effect of thrust disk inclination angle on the (<b>a</b>) direct translational stiffness and (<b>b</b>) damping coefficients of the thrust-type foil bearings under different bump foil thickness ratios (rotational speed = 2.5 × 10<sup>4</sup> r·min<sup>−1</sup>, <span class="html-italic">N</span> = 5, <span class="html-italic">h</span><sub>2</sub> = 10 μm, <span class="html-italic">μ</span> = 0.1, <span class="html-italic">η</span> = 0.1).</p>
Full article ">
Back to TopTop