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Actuators
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Flow Control and Beyond Enhancing Performance and Energy Efficiency in...
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Flow Control and Beyond Enhancing Performance and Energy Efficiency in Complex Fluid System

A special issue of Actuators (ISSN 2076-0825). This special issue belongs to the section "High Torque/Power Density Actuators".

Deadline for manuscript submissions: 30 September 2025 | Viewed by 2787

Special Issue Editors

Dr. Frederico Miguel Freire Rodrigues

E-Mail Website
Guest Editor
Department of Electromechanical Engineering, University of Beira Interior, 6200386 Covilhã, Portugal
Interests: renewable energies; plasma actuators; aerodynamics; fluid mechanics; heat transfer
Special Issues, Collections and Topics in MDPI journals
Dr. M. Abdollahzadeh

E-Mail Website
Guest Editor
C-MAST, Department of Electromechanical Engineering, Universidade da Beira Interior Portugal, 6200 Covilhã, Portugal
Interests: flow control; atmospheric deicing devices; plasma actuators; energy conversion and energy storage; numerical simulation; enhanced heat transfer; redox flow batteries
Special Issues, Collections and Topics in MDPI journals

Special Issue Information

Dear Colleagues,

This Special Issue aims to attract works related to a diverse range of topics on the implementation of actuators for flow control in complex fluid systems. Fluid systems play a pivotal role in several industrial applications. The ability to manipulate and control flow fields is key for achieving considerable energy efficiency and performance enhancements. Bearing this in mind, this Special Issue intends to disseminate the most recent advances on various themes related to flow control, including the following: advanced flow control techniques; electro-hydro dynamics and magneto-plasma dynamics; novel fluid dynamic modeling approaches; the interplay between flow control techniques; novel actuators for fluid flow manipulation; cutting-edge materials and technologies for active and passive flow control; machine learning methods for smart flow control; and interdisciplinary research at the intersection of fluid dynamics, engineering, and sustainability.

Dr. Frederico Miguel Freire Rodrigues
Dr. M. Abdollahzadeh
Guest Editors

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Submitted manuscripts should not have been published previously, nor be under consideration for publication elsewhere (except conference proceedings papers). All manuscripts are thoroughly refereed through a single-blind peer-review process. A guide for authors and other relevant information for submission of manuscripts is available on the Instructions for Authors page. Actuators is an international peer-reviewed open access monthly journal published by MDPI.

Please visit the Instructions for Authors page before submitting a manuscript. The Article Processing Charge (APC) for publication in this open access journal is 2400 CHF (Swiss Francs). Submitted papers should be well formatted and use good English. Authors may use MDPI's English editing service prior to publication or during author revisions.

Keywords

  • flow control
  • actuators
  • fluid systems
  • electro-hydro dynamics
  • magneto-plasma dynamics

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Published Papers (5 papers)

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Research

17 pages, 1151 KiB  
Article
Numerical Analysis of a Hypersonic Body Under Thermochemical Non-Equilibrium and Different Catalytic Surface Conditions
by Odelma Teixeira and José Páscoa
Actuators 2025, 14(2), 102; https://doi.org/10.3390/act14020102 - 19 Feb 2025
Viewed by 135
Abstract
This work results from a numerical investigation of the thermochemical non-equilibrium effects on the surface properties of a hypersonic body. Non-equilibrium within an air mixture composed of 11 chemical species was considered when solving the Navier–Stokes–Fourier equations using a density-based algorithm in OpenFOAM. [...] Read more.
This work results from a numerical investigation of the thermochemical non-equilibrium effects on the surface properties of a hypersonic body. Non-equilibrium within an air mixture composed of 11 chemical species was considered when solving the Navier–Stokes–Fourier equations using a density-based algorithm in OpenFOAM. The influence of thermal and chemical non-equilibrium on the surface properties of a hypersonic double-cone test body was studied by considering two types of surfaces. It was found that the heat flux and pressure distribution along the surface are higher under non-equilibrium free-stream conditions. Unlike what was observed at the impingement point, where the vibrational non-equilibrium effects on the surface properties are almost independent of the surface type, at the stagnation point, these effects are highly dependent on the catalytic activity of the surface. At the stagnation point, the vibrational non-equilibrium effects are more pronounced on a fully catalytic surface than on a non-catalytic surface. Under the studied conditions, the vibrational non-equilibrium reduces the heat flux by 18% for a non-catalytic surface, while for a fully catalytic surface, it reduces the heat flux by 38%. Additionally, the presence of vibrational non-equilibrium in the free-stream reduces the pressure by 24% for a non-catalytic surface, while for a fully catalytic surface, it is reduced by 42%. Full article
(This article belongs to the Special Issue Flow Control and Beyond Enhancing Performance and Energy Efficiency in Complex Fluid System)
►▼ Show Figures

Figure 1

Figure 1
<p>Simulation model diagram.</p> Full article ">Figure 2
<p>Double-cone model: (<b>a</b>) geometric parameters (dimensions in cm); (<b>b</b>) solution domain and boundary conditions.</p> Full article ">Figure 3
<p>Code validation: (<b>a</b>) heat flux; (<b>b</b>) pressure. Distribution along the double-cone surface.</p> Full article ">Figure 4
<p>Grid convergence analysis: (<b>a</b>) maximum heat flux location; (<b>b</b>) size of the separation zone.</p> Full article ">Figure 5
<p>Pressure contours considering five-species (top) and eleven-species air mixtures (bottom).</p> Full article ">Figure 6
<p>Vibro-electronic temperature contours at equilibrium and non-equilibrium free-stream conditions for: (<b>a</b>) five-species air mixture; (<b>b</b>) eleven-species air mixture.</p> Full article ">Figure 7
<p>Surface heat flux distribution along the double-cone surface for five-species and eleven-species air mixtures for different free-stream conditions: (<b>a</b>) equilibrium; (<b>b</b>) non-equilibrium.</p> Full article ">Figure 8
<p>Surface pressure distribution along the double-cone surface for five-species and eleven-species air mixture for different free-stream conditions: (<b>a</b>) equilibrium; (<b>b</b>) non-equilibrium.</p> Full article ">Figure 9
<p>Distribution of surface properties for equilibrium and non-equilibrium conditions: (<b>a</b>) heat flux; (<b>b</b>) pressure. Comparison between non-catalytic surface (NCS) and fully catalytic surface (FCS).</p> Full article ">Figure 10
<p>Distribution of flow properties along the impingement point line (Y = 0.052 m) for equilibrium and non-equilibrium conditions: (<b>a</b>) pressure; (<b>b</b>) trans-rotational temperature (<math display="inline"><semantics> <msub> <mi mathvariant="normal">T</mi> <mrow> <mi>t</mi> <mi>r</mi> </mrow> </msub> </semantics></math>); (<b>c</b>) vibro-electronic temperature (<math display="inline"><semantics> <msub> <mi mathvariant="normal">T</mi> <mrow> <mi>v</mi> <mi>e</mi> </mrow> </msub> </semantics></math>). Comparison between non-catalytic surface (NCS) and fully catalytic surface (FCS).</p> Full article ">Figure 11
<p>Temperature distributions along the stagnation line (Y = 0 m) for equilibrium and non-equilibrium conditions: (<b>a</b>) trans-rotational (<math display="inline"><semantics> <msub> <mi mathvariant="normal">T</mi> <mrow> <mi>t</mi> <mi>r</mi> </mrow> </msub> </semantics></math>); (<b>b</b>) vibro-electronic temperature (<math display="inline"><semantics> <msub> <mi mathvariant="normal">T</mi> <mrow> <mi>v</mi> <mi>e</mi> </mrow> </msub> </semantics></math>). Comparison between non-catalytic surface (NCS) and fully catalytic surface (FCS).</p> Full article ">
16 pages, 6815 KiB  
Article
Investigating the Power Extraction of Applying Hybrid Pitching Motion on a Wing with Leading and Trailing Flaps
by Suleiman Saleh and Chang-Hyun Sohn
Actuators 2025, 14(2), 62; https://doi.org/10.3390/act14020062 - 27 Jan 2025
Viewed by 575
Abstract
This research utilized a hybrid trajectory on a wing incorporating a dual flap with the goal of enhancing performance. The hybrid profiles initiate with a non-sinusoidal pattern during the interval 0.0 ≤ t/T ≤ 0.25, evolving toward a sinusoidal pattern within the range [...] Read more.
This research utilized a hybrid trajectory on a wing incorporating a dual flap with the goal of enhancing performance. The hybrid profiles initiate with a non-sinusoidal pattern during the interval 0.0 ≤ t/T ≤ 0.25, evolving toward a sinusoidal pattern within the range 0.25 < t/T ≤ 0.5. Similarly, the hybrid motion follows a non-sinusoidal pattern in the range 0.5 < t/T ≤ 0.75, before shifting back to a sinusoidal pattern within the range 0.75 < t/T ≤ 1.0. The effectiveness of using a hybrid trajectory on a wing with leading and trailing flaps in enhancing the energy harvesting performance is examined through numerical simulations. The results demonstrate that hybrid trajectories applied to a two-flap wing configuration outperform a single flat plate and a wing with leading and trailing flaps both operating under a sinusoidal trajectory. The wing length spans from 45% to 55%, with the leading flap length ranging from 25% to 35%. The trailing flap lengths adjust accordingly to ensure the combined total matches the flat plate’s full length, which is 100%. The wing pitch angle was fixed at 85° while the leading flap’s pitch angle varied between 40° and 55° and the pitch angle of the trailing flap ranged from 0° to 20°. The findings reveal that utilizing hybrid motion on a wing fitted with leading and trailing flaps notably improves power output in comparison to configurations with either one plate or three plates. The power output is achieved at particular dimensions: a leading flap length of 30%, a wing length of 55%, and a trailing flap length of 15%. The corresponding pitch angles are 50° for the leading flap, 85° for the wing, and 10° for the trailing flap. The aforementioned configuration results in a 34.06% increase in output power in comparison to one plate. The maximum efficiency for this setup reaches 44.21%. This underscores the superior performance of hybrid trajectories over sinusoidal trajectories in enhancing energy extraction performance. Full article
(This article belongs to the Special Issue Flow Control and Beyond Enhancing Performance and Energy Efficiency in Complex Fluid System)
►▼ Show Figures

Figure 1

Figure 1
<p>Illustrations of a wing using two flaps.</p> Full article ">Figure 2
<p>Kinematics of (<b>a</b>) a single flat plate; (<b>b</b>) a wing with leading and trailing flaps.</p> Full article ">Figure 3
<p>Pitch angle profiles: (<b>a</b>) sinusoidal; (<b>b</b>) non-sinusoidal; (<b>c</b>) hybrid motions.</p> Full article ">Figure 4
<p>Shows (<b>a</b>) computational domain; (<b>b</b>) sub-region; and (<b>c</b>) closeup view.</p> Full article ">Figure 5
<p>Analysis of (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="normal">C</mi> </mrow> <mrow> <mi mathvariant="normal">L</mi> </mrow> </msub> </mrow> </semantics></math> [<a href="#B57-actuators-14-00062" class="html-bibr">57</a>] and (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="normal">C</mi> </mrow> <mrow> <mi mathvariant="normal">p</mi> <mi mathvariant="normal">l</mi> </mrow> </msub> </mrow> </semantics></math> [<a href="#B57-actuators-14-00062" class="html-bibr">57</a>] in turbulent flow.</p> Full article ">Figure 6
<p>The calculated results for (<b>a</b>) total power coefficient and (<b>b</b>) efficiency for Cases 2 and 4.</p> Full article ">Figure 7
<p>Comparison of (<b>a</b>) pushing force coefficient, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="normal">C</mi> </mrow> <mrow> <mi mathvariant="normal">L</mi> </mrow> </msub> </mrow> </semantics></math>(t); (<b>b</b>) pushing power coefficient, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="normal">C</mi> </mrow> <mrow> <mi mathvariant="normal">p</mi> <mi mathvariant="normal">l</mi> </mrow> </msub> </mrow> </semantics></math>; (<b>c</b>) moment coefficient, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="normal">C</mi> </mrow> <mrow> <mi mathvariant="normal">M</mi> </mrow> </msub> </mrow> </semantics></math>; (<b>d</b>) moment power coefficient, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="normal">C</mi> </mrow> <mrow> <mi mathvariant="normal">p</mi> <mi mathvariant="normal">m</mi> </mrow> </msub> </mrow> </semantics></math>; (<b>e</b>) total power coefficient, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="normal">C</mi> </mrow> <mrow> <mi mathvariant="normal">p</mi> <mi mathvariant="normal">t</mi> </mrow> </msub> </mrow> </semantics></math>.</p> Full article ">Figure 7 Cont.
<p>Comparison of (<b>a</b>) pushing force coefficient, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="normal">C</mi> </mrow> <mrow> <mi mathvariant="normal">L</mi> </mrow> </msub> </mrow> </semantics></math>(t); (<b>b</b>) pushing power coefficient, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="normal">C</mi> </mrow> <mrow> <mi mathvariant="normal">p</mi> <mi mathvariant="normal">l</mi> </mrow> </msub> </mrow> </semantics></math>; (<b>c</b>) moment coefficient, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="normal">C</mi> </mrow> <mrow> <mi mathvariant="normal">M</mi> </mrow> </msub> </mrow> </semantics></math>; (<b>d</b>) moment power coefficient, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="normal">C</mi> </mrow> <mrow> <mi mathvariant="normal">p</mi> <mi mathvariant="normal">m</mi> </mrow> </msub> </mrow> </semantics></math>; (<b>e</b>) total power coefficient, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="normal">C</mi> </mrow> <mrow> <mi mathvariant="normal">p</mi> <mi mathvariant="normal">t</mi> </mrow> </msub> </mrow> </semantics></math>.</p> Full article ">Figure 8
<p>The plots of vorticity for Case 4 at various leading pitch angles and time steps: (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mo>ψ</mo> </mrow> <mrow> <mi mathvariant="normal">o</mi> </mrow> </msub> </mrow> </semantics></math> = 45°; (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mo>ψ</mo> </mrow> <mrow> <mi mathvariant="normal">o</mi> </mrow> </msub> </mrow> </semantics></math> = 50°; and (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mo>ψ</mo> </mrow> <mrow> <mi mathvariant="normal">o</mi> </mrow> </msub> </mrow> </semantics></math> = 55°.</p> Full article ">Figure 9
<p>Pressure coefficient for Case 4 at various leading flap pitch angles and time steps: (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mo>ψ</mo> </mrow> <mrow> <mi mathvariant="normal">o</mi> </mrow> </msub> </mrow> </semantics></math> = 45°; (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mo>ψ</mo> </mrow> <mrow> <mi mathvariant="normal">o</mi> </mrow> </msub> </mrow> </semantics></math> = 50°; and (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mo>ψ</mo> </mrow> <mrow> <mi mathvariant="normal">o</mi> </mrow> </msub> </mrow> </semantics></math> = 55°.</p> Full article ">Figure 10
<p>Average total power coefficient (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="normal">C</mi> </mrow> <mrow> <mi mathvariant="normal">p</mi> <mi mathvariant="normal">t</mi> </mrow> </msub> </mrow> </semantics></math>) for a wing with two flaps using a hybrid pitching motion: (<b>a</b>) LF25%, W55%, TF20%; (<b>b</b>) LF30%, W50%, TF20%; (<b>c</b>) LF30%, W55%, TF15%; and (<b>d</b>) LF35%, W45%, TF20% for Case 4 at wing pitch angle = 85° and various flap pitch angles.</p> Full article ">
21 pages, 4819 KiB  
Article
Methane/Air Flame Control in Non-Premixed Bluff Body Burners Using Ring-Type Plasma Actuators
by Fatemeh Bagherighajari, Mohammadmahdi Abdollahzadehsangroudi and José C. Páscoa
Actuators 2025, 14(2), 47; https://doi.org/10.3390/act14020047 - 22 Jan 2025
Viewed by 495
Abstract
Enhancing the combustion efficiency and flame stability in conventional systems is essential for reducing carbon emissions and advancing sustainable energy solutions. In this context, electrohydrodynamic plasma actuators offer a promising active control method for modifying and regulating flame characteristics. This study presents a [...] Read more.
Enhancing the combustion efficiency and flame stability in conventional systems is essential for reducing carbon emissions and advancing sustainable energy solutions. In this context, electrohydrodynamic plasma actuators offer a promising active control method for modifying and regulating flame characteristics. This study presents a numerical investigation into the effects of a ring-type plasma actuator positioned on the co-flow air side of a non-premixed turbulent methane/air combustion system—an approach not previously reported in the literature. The ring-type plasma actuator was designed by placing electrodes along the perimeter of the small diameter wall of the air duct. The impact of the plasma actuator on the reacting flow field within the burner was analyzed, with a focus on its influence on the flow dynamics and flame structure. The results, visualized through velocity and temperature contours, as well as flow streamlines, provide insight into the actuator’s effect on flame behavior. Two operating modes of the plasma actuators were evaluated: co-flow mode, where the aerodynamic effect of the plasma actuators was directed downstream; and counter-flow mode, where the effects were directed upstream. The findings indicate that the co-flow actuation positively reduces the flame height and enhances the flame anchoring at the root, whereas counter-flow actuation slightly weakens the flame root. Numerical simulations further revealed that co-flow actuation marginally increases the energy release by approximately 0.13%, while counter-flow actuation reduces the energy release by around 7.8%. Full article
(This article belongs to the Special Issue Flow Control and Beyond Enhancing Performance and Energy Efficiency in Complex Fluid System)
►▼ Show Figures

Figure 1

Figure 1
<p>Schematic of a single DBD plasma actuator, including the normalized governing equations and boundary conditions for the phenomenological model of the plasma actuator.</p> Full article ">Figure 2
<p>Comparison of the present study’s results for the net thrust generated by the linear plasma actuator with (<b>a</b>) the experimental results of Thomas et al. [<a href="#B32-actuators-14-00047" class="html-bibr">32</a>] and (<b>b</b>) the experimental results of Durscher and Roy [<a href="#B33-actuators-14-00047" class="html-bibr">33</a>].</p> Full article ">Figure 3
<p>Comparison of the plasma-induced velocity profiles from the present study with the experimental results of (<b>a</b>) Thomas et al. [<a href="#B32-actuators-14-00047" class="html-bibr">32</a>] and (<b>b</b>) Durscher and Roy [<a href="#B33-actuators-14-00047" class="html-bibr">33</a>].</p> Full article ">Figure 4
<p>Comparison of the axial and radial velocity profiles with experimental data from (<b>a</b>,<b>b</b>) Dally et al. [<a href="#B20-actuators-14-00047" class="html-bibr">20</a>], (<b>c</b>,<b>d</b>) Tong et al. [<a href="#B36-actuators-14-00047" class="html-bibr">36</a>], and (<b>e</b>) Caetano and da Silva [<a href="#B37-actuators-14-00047" class="html-bibr">37</a>].</p> Full article ">Figure 5
<p>Comparison of the simulation results for the (<b>a</b>,<b>b</b>) temperature profiles and (<b>c</b>) axial and (<b>d</b>) radial velocity profiles for the reacting flow regime with the experimental data of Dally et al. [<a href="#B20-actuators-14-00047" class="html-bibr">20</a>].</p> Full article ">Figure 6
<p>Schematic of the bluff body burner equipped with a ring DBD plasma actuator in the air co-flow stream.</p> Full article ">Figure 7
<p>Computational grid of the burner equipped with a ring DBD plasma actuator.</p> Full article ">Figure 8
<p>Results of grid sensitivity study, based on the variation of the maximum temperatures inside the burner for different grid cell counts.</p> Full article ">Figure 9
<p>Velocity contours with flow streamlines: (<b>a</b>) without the plasma actuator; (<b>b</b>) with the plasma actuator in the co-flow configuration; (<b>c</b>) with the plasma actuator in the counter-flow configuration.</p> Full article ">Figure 10
<p>Temperature contours representing the flame structure: (<b>a</b>) without the plasma actuator; (<b>b</b>) with the plasma actuator in the co-flow configuration; (<b>c</b>) with the plasma actuator in the counter-flow configuration.</p> Full article ">Figure 11
<p>Plot of the differences in temperature between (<b>a</b>) the co-flow and no actuator case and (<b>b</b>) the counter-flow and no actuator case.</p> Full article ">Figure 12
<p>Temperature profiles for the cases without the plasma actuator and with the plasma actuator in the co-flow and counter-flow configurations at (<b>a</b>) x/D<sub>b</sub> = 0.167, (<b>b</b>) x/D<sub>b</sub> = 1.34, and (<b>c</b>) x/D<sub>b</sub> = 4.167 downstream of the bluff body.</p> Full article ">
24 pages, 10928 KiB  
Article
Three-Dimensional Pulsating Flow Simulation in a Multi-Point Gas Admission Valve for Large-Bore CNG Engines
by Soo-Jin Jeong and Seong-Joon Moon
Actuators 2024, 13(12), 492; https://doi.org/10.3390/act13120492 - 2 Dec 2024
Viewed by 543
Abstract
This study examines the dynamic fluid behavior of a PWM-controlled Solenoid-Operated Gas Admission Valve (SOGAV) for large-bore CNG engines using 3D Computational Fluid Dynamics (CFD) simulations with dynamic mesh techniques. The research focuses on the influence of orifice geometry variations in the multi-hole [...] Read more.
This study examines the dynamic fluid behavior of a PWM-controlled Solenoid-Operated Gas Admission Valve (SOGAV) for large-bore CNG engines using 3D Computational Fluid Dynamics (CFD) simulations with dynamic mesh techniques. The research focuses on the influence of orifice geometry variations in the multi-hole restrictor and pressure differentials between the inlet and outlet on flow stability, turbulence, and valve performance. Results demonstrate that multi-hole restrictors with different-sized orifices improve flow uniformity and reduce turbulence, thereby mitigating flow resistance. Transient simulations further reveal standing wave formation and pressure wave interference, emphasizing that steady-state models cannot capture critical transient phenomena, such as accelerated and decelerated jet-like flows and flow separation. These findings provide key insights into SOGAV optimization, contributing to enhanced fuel efficiency and engine responsiveness, meeting the performance requirements of modern gas engines. Full article
(This article belongs to the Special Issue Flow Control and Beyond Enhancing Performance and Energy Efficiency in Complex Fluid System)
►▼ Show Figures

Figure 1

Figure 1
<p>A cross-sectional view of the SOGAV 105, developed by Woodward [<a href="#B6-actuators-13-00492" class="html-bibr">6</a>].</p> Full article ">Figure 2
<p>Structure of the three main components of the SOGAV.</p> Full article ">Figure 3
<p>Schematic diagram of sequence of flow direction.</p> Full article ">Figure 4
<p>Hexahedral computational mesh system of flow domain of SOGAV. (<b>a</b>) 3D grid model for the entire computational domain; (<b>b</b>) 2D mesh structure at cross-section A.</p> Full article ">Figure 5
<p>Schematic diagram of the complete geometric configuration and dimensions of the computational domain, along with the specified locations of the applied boundary conditions.</p> Full article ">Figure 6
<p>Schematic representation of the hole arrangement configurations for the three multi-hole restrictors evaluated in this study: (<b>a</b>) base model; (<b>b</b>) model with only large holes; (<b>c</b>) model with enlarged large holes.</p> Full article ">Figure 7
<p>Lift curves of moving plate with respect to time: (<b>a</b>) operating frequency of 8.3 Hz (<b>b</b>) operating frequency of 4.9 Hz.</p> Full article ">Figure 8
<p>Sectional plots of velocity distributions and flow uniformities within SOGAV: (<b>a</b>) Case 1 and 3; (<b>b</b>) Case 2 and 4.</p> Full article ">Figure 9
<p>An enlarged view of the velocity vector fields in Zones A and B: (<b>a</b>) Zone A; (<b>b</b>) Zone B.</p> Full article ">Figure 10
<p>Graph of axial variations of the cross-sectional average pressure of SOGAV for Case 1 and Case 3.</p> Full article ">Figure 11
<p>Velocity distribution at cross-section A of the SOGAV as a function of temporal variations in moving plate lift: (<b>a</b>) Point 1/4 lift; (<b>b</b>) Point MOO; (<b>c</b>) Point B; (<b>d</b>) Point C; (<b>e</b>) Point MOC; (<b>f</b>) 1/4 lift.</p> Full article ">Figure 12
<p>velocity distributions at cross-section B as a function of the moving plate’s lift variations: (<b>a</b>) point MOO; (<b>b</b>) point B; (<b>c</b>); (<b>d</b>)point MOC.</p> Full article ">Figure 13
<p>Transient profiles of flow uniformity for different running conditions.</p> Full article ">Figure 14
<p>Pressure pulsations at the mid-point of the outlet pipe for different running conditions.</p> Full article ">Figure 15
<p>Temporal variations of mass flow rate at the exit of the outlet pipe for different running conditions.</p> Full article ">Figure 16
<p>Pressure pulsations at the mid-point of the outlet pipe for different orifice geometries.</p> Full article ">Figure 17
<p>Temporal variations of mass flow rate at the exit of the outlet pipe for different orifice geometries.</p> Full article ">Figure 18
<p>Pressure wave patterns in intake pipe of SOGAV for Case 1.</p> Full article ">Figure 19
<p>Pressure wave patterns in intake pipe of SOGAV for Case 2.</p> Full article ">
22 pages, 11914 KiB  
Article
Analysis of Dynamic Flow Loss of High Water-Based Emulsion Pump
by Lirong Wan, Yuang Yin, Zhiyuan Sun, Gaozuo Sun, Guoqing Qi and Ruwei Zhang
Actuators 2024, 13(12), 482; https://doi.org/10.3390/act13120482 - 28 Nov 2024
Viewed by 562
Abstract
The emulsion pump’s flow loss directly affects its performance and efficiency. However, the annular plunger chamber leakage and valve core hysteresis are challenging to avoid during operation. This study systematically investigated the impact of the annular gap in the plunger cavity on emulsion [...] Read more.
The emulsion pump’s flow loss directly affects its performance and efficiency. However, the annular plunger chamber leakage and valve core hysteresis are challenging to avoid during operation. This study systematically investigated the impact of the annular gap in the plunger cavity on emulsion pump performance. Using theoretical analysis and computational fluid dynamics methods, it explored the mechanism of the port valve hysteresis during discharge. The simulation results show that the leakage of the annular gap is proportional to the gap thickness and the inlet pressure and inversely proportional to the dynamic viscosity of the emulsion. With the increase of plunger eccentricity, the leakage increases slowly. The increase in the outlet diameter of the port valve will lead to more significant hysteresis of the valve core. The change of outlet pressure has little effect on the hysteresis and flow of the spool, and the response speed of the wing-guided bevel discharge valve is faster than that of the ordinary poppet valve. Considering the above factors, the flow distribution process of the emulsion pump can be accurately analyzed, providing a reference for pump optimization. Full article
(This article belongs to the Special Issue Flow Control and Beyond Enhancing Performance and Energy Efficiency in Complex Fluid System)
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Figure 1
<p>Emulsion pump structure model.</p> Full article ">Figure 2
<p>Diagram of plunger motion.</p> Full article ">Figure 3
<p>Port valve structure diagram.</p> Full article ">Figure 4
<p>Sketch of plunger motion.</p> Full article ">Figure 5
<p>Plunger gap leakage model.</p> Full article ">Figure 6
<p>(<b>a</b>) Instantaneous outlet flow and (<b>b</b>) total leakage under different inlet pressures.</p> Full article ">Figure 7
<p>(<b>a</b>) Instantaneous outlet flow and (<b>b</b>) total leakage under different dynamic viscosities.</p> Full article ">Figure 8
<p>(<b>a</b>) Instantaneous outlet flow and (<b>b</b>) total leakage under different gap thicknesses.</p> Full article ">Figure 9
<p>Sketch of plunger motion when the plunger is eccentric.</p> Full article ">Figure 10
<p>Three-dimensional expansion diagram of gap thickness when the plunger is eccentric.</p> Full article ">Figure 11
<p>Comparison diagram of flow velocity and pressure when the plunger is eccentric.</p> Full article ">Figure 12
<p>(<b>a</b>) Instantaneous outlet flow and (<b>b</b>) total leakage at different eccentricities.</p> Full article ">Figure 13
<p>Sketch of plunger motion when the plunger is in inclination.</p> Full article ">Figure 14
<p>Three-dimensional expansion diagram of gap thickness when the plunger is inclined.</p> Full article ">Figure 15
<p>Comparison diagram of velocity and pressure when the plunger is inclined.</p> Full article ">Figure 16
<p>(<b>a</b>) Instantaneous outlet flow and (<b>b</b>) total leakage at different inclination angles.</p> Full article ">Figure 17
<p>Port valve model.</p> Full article ">Figure 18
<p>(<b>a</b>) Verification of mesh independence of the discharge valve and (<b>b</b>) verification of mesh independence of the suction valve.</p> Full article ">Figure 19
<p>(<b>a</b>) Flow velocity and (<b>b</b>) pressure diagram of suction valve port.</p> Full article ">Figure 20
<p>Suction valve spool displacement and instantaneous leakage.</p> Full article ">Figure 21
<p>(<b>a</b>) Flow velocity and (<b>b</b>) pressure diagram of the valve port of the discharge valve.</p> Full article ">Figure 22
<p>Comparison chart of spool displacement and instantaneous outlet flow of discharge valve.</p> Full article ">Figure 23
<p>Comparison diagram of velocity and pressure at different outlet diameters.</p> Full article ">Figure 24
<p>(<b>a</b>) Spool displacement and (<b>b</b>) instantaneous outlet flow rate under different outlet diameters.</p> Full article ">Figure 25
<p>(<b>a</b>) Valve port pressure and (<b>b</b>) valve port speed under different outlet pressures.</p> Full article ">Figure 26
<p>Valve port pressure difference under different outlet pressures.</p> Full article ">Figure 27
<p>(<b>a</b>) Spool displacement and (<b>b</b>) instantaneous outlet flow under different outlet pressures.</p> Full article ">Figure 28
<p>(<b>a</b>) Flow velocity and (<b>b</b>) pressure diagram of plane cone valve port.</p> Full article ">Figure 29
<p>Effect of guide vane structure on (<b>a</b>) spool displacement and (<b>b</b>) instantaneous outlet flow.</p> Full article ">
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