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19 pages, 5183 KiB  
Review
Development of Optical Fiber Light-Transmitting Concrete (LTC)—A Review
by Jian Bai, Weiguo Zhang, Jun Tian, Xiaowei Wu and Mingfang Zheng
Buildings 2025, 15(1), 104; https://doi.org/10.3390/buildings15010104 - 31 Dec 2024
Viewed by 335
Abstract
In recent years, the use of new and unique building materials to achieve green building goals has attracted a lot of attention. Optical fiber light-transmitting concrete (LTC) makes it possible for light to pass through concrete. Its ornamental value and excellent light transmission [...] Read more.
In recent years, the use of new and unique building materials to achieve green building goals has attracted a lot of attention. Optical fiber light-transmitting concrete (LTC) makes it possible for light to pass through concrete. Its ornamental value and excellent light transmission have received much attention from scholars. However, the application of optical fiber LTC in the construction industry has not yet been promoted due to the tedious preparation process and insufficient research on its mechanical properties and durability. This paper reviews the research results of optical fiber LTC in terms of product preparation, light transmission, mechanical properties, durability, and microstructures. The light transmission of optical fiber LTCs is positively correlated with fiber content and negatively correlated with fiber diameter and fiber spacing. However, how the combination of these factors affects LTC transmittance remains to be investigated. In addition to fiber parameters, cement matrix properties and other environmental factors (light intensity, incidence angle, and aging) should also be considered to explore the suitability of LTC. The fiber–matrix interface bond strength needs further investigation and efforts should be made to improve it. This paper also summarizes the future challenges and research directions of optical fiber LTC, which is expected to provide guidance for the application of optical fiber LTC. It is anticipated that fiber-optic LTC will be promoted as a new building material. Full article
(This article belongs to the Special Issue Advanced Research on Cementitious Composites for Construction)
Show Figures

Figure 1

Figure 1
<p>Light-transmitting concrete (LTC). (<b>a</b>) Light transmission effect of LTC (<a href="https://zhuanlan.zhihu.com/p/439568476" target="_blank">https://zhuanlan.zhihu.com/p/439568476</a> (1 December 2024)). (<b>b</b>) Light transmission diagram of LTC.</p>
Full article ">Figure 2
<p>Light-conducting materials and areas of application for LTC.</p>
Full article ">Figure 3
<p>Structure of optical fiber: (<b>a</b>) Structure of optical fiber. (<b>b</b>) multimode step-index. (<b>c</b>) multimode graded-index. (<b>d</b>) single-mode (Δt: pulse width).</p>
Full article ">Figure 4
<p>Preparation of fiber fabric [<a href="#B31-buildings-15-00104" class="html-bibr">31</a>,<a href="#B32-buildings-15-00104" class="html-bibr">32</a>].</p>
Full article ">Figure 5
<p>Fiber fixation and cement mortar placement [<a href="#B33-buildings-15-00104" class="html-bibr">33</a>].</p>
Full article ">Figure 6
<p>Fiber-optic transmission concrete fiber implantation and cement base placement [<a href="#B34-buildings-15-00104" class="html-bibr">34</a>].</p>
Full article ">Figure 7
<p>Photometer and optical power meter [<a href="#B32-buildings-15-00104" class="html-bibr">32</a>].</p>
Full article ">Figure 8
<p>The influence of fiber content, spacing, and diameter on transmittance and the relationships among them [<a href="#B1-buildings-15-00104" class="html-bibr">1</a>,<a href="#B2-buildings-15-00104" class="html-bibr">2</a>,<a href="#B6-buildings-15-00104" class="html-bibr">6</a>,<a href="#B10-buildings-15-00104" class="html-bibr">10</a>,<a href="#B36-buildings-15-00104" class="html-bibr">36</a>,<a href="#B37-buildings-15-00104" class="html-bibr">37</a>]. (<b>a</b>) Relationship between fiber content and transmittance. (<b>b</b>) Relationship between fiber diameter and transmittance. (<b>c</b>) Relationship between optical fiber spacing and optical fiber diameter.</p>
Full article ">Figure 9
<p>Comparison of compressive and bending strengths of LTC based on different fiber contents [<a href="#B2-buildings-15-00104" class="html-bibr">2</a>,<a href="#B9-buildings-15-00104" class="html-bibr">9</a>,<a href="#B31-buildings-15-00104" class="html-bibr">31</a>,<a href="#B32-buildings-15-00104" class="html-bibr">32</a>,<a href="#B33-buildings-15-00104" class="html-bibr">33</a>,<a href="#B35-buildings-15-00104" class="html-bibr">35</a>,<a href="#B36-buildings-15-00104" class="html-bibr">36</a>,<a href="#B37-buildings-15-00104" class="html-bibr">37</a>]. (<b>a</b>) The relationship between compressive strength and fiber content. (<b>b</b>) the relationship between flexural strength and fiber content.</p>
Full article ">Figure 10
<p>Influence of fiber diameter on the LTC compressive strength of fiber. (<b>a</b>) The compressive strength increases with the increase in the diameter of the optical fiber. (<b>b</b>) the compressive strength increases and then decreases with increasing fiber diameter.</p>
Full article ">Figure 11
<p>The microscopic picture of the optical fiber LTC interface [<a href="#B31-buildings-15-00104" class="html-bibr">31</a>,<a href="#B32-buildings-15-00104" class="html-bibr">32</a>,<a href="#B35-buildings-15-00104" class="html-bibr">35</a>]. (<b>a</b>) Fiber untreated. (<b>b</b>) fiber treated.</p>
Full article ">Figure 12
<p>Excellent examples of transparent concrete in the construction field. (<b>a</b>) Fruangen Church. (<b>b</b>) Celia Septichora Museum. (<b>c</b>) Fruangen Church. (<b>d</b>) Italy pavilion of 2010 Shanghai Expo.</p>
Full article ">Figure 13
<p>Application of transparent concrete in interior design.</p>
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<p>LTC road design. (<b>a</b>) Park pavement. (<b>b</b>) Highways.</p>
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<p>Price comparison of various translucent materials [<a href="#B2-buildings-15-00104" class="html-bibr">2</a>].</p>
Full article ">
20 pages, 12914 KiB  
Article
Crossing and Anticrossing in Bent All-Glass Leakage Channel Microstructured Optical Fibers: The Effect of Polymer Coating
by Alexander N. Denisov, Vladislav V. Dvoyrin and Sergey L. Semjonov
Photonics 2024, 11(12), 1204; https://doi.org/10.3390/photonics11121204 - 22 Dec 2024
Viewed by 374
Abstract
This paper presents the results of a detailed theoretical study of the bending properties of all-glass leakage channel microstructured optical fibers (LC MOFs) with a polymer coating over a bending radius range from 4.8 cm to 10 cm. The dependencies of the effective [...] Read more.
This paper presents the results of a detailed theoretical study of the bending properties of all-glass leakage channel microstructured optical fibers (LC MOFs) with a polymer coating over a bending radius range from 4.8 cm to 10 cm. The dependencies of the effective refractive indices of the LC MOF modes on the bending radius have a number of crossings and anticrossings for different mode pairs. A detailed analysis showed that eight modes for each polarization have to be considered to correctly calculate the bending losses. These modes can be classified into relatively strong modes (three for each polarization) and relatively weak modes. The three strong modes have the most direct effect on the loss calculation. However, the relatively weaker modes also play a role through their coupling with the stronger modes, resulting in the appearance of local loss maxima in the loss dependencies for the strong modes. At a bending radius of 10 cm, the final leakage loss of the LC MOFs with a polymer coating is approximately four times lower than that of the LC MOFs without a coating. The significant reduction in losses paves the way for further optimization of the LC MOF geometric structure, leading to a reduction in the allowable bending radius. Full article
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Figure 1

Figure 1
<p>Structure of MOF-18 with polymer coating: <span class="html-italic">d</span><sub>1</sub>/Λ<sub>1</sub> = 0.82; <span class="html-italic">d</span><sub>2</sub>/<span class="html-italic">d</span><sub>1</sub> = 1.25; <span class="html-italic">d</span><sub>3</sub>/<span class="html-italic">d</span><sub>1</sub> = 0.90; Λ<sub>2</sub>/Λ<sub>1</sub> = 1.25; and Λ<sub>3</sub>/Λ<sub>1</sub> = 1.10.</p>
Full article ">Figure 2
<p>(<b>a</b>) Spatial distribution of <span class="html-italic">n</span><sub>equ</sub> across MOF-18 cross-section for <span class="html-italic">R</span> = 0.048 m; (<b>b</b>) profile of <span class="html-italic">n</span><sub>equ</sub> along MOF-18 cross-section for <span class="html-italic">y</span> = 0 at <span class="html-italic">R</span> = 0.048 m.</p>
Full article ">Figure 3
<p>Spatial intensity distributions of different modes polarized along <span class="html-italic">x</span>-axis for selected bending radii <span class="html-italic">R</span>: (<b>a</b>) Mode 1a, <span class="html-italic">R</span> = 5.92 cm; (<b>b</b>) Mode 1b, <span class="html-italic">R</span> = 5.98 cm; (<b>c</b>) Mode 1c, <span class="html-italic">R</span> = 5.88 cm; (<b>d</b>) Mode 1d, <span class="html-italic">R</span> = 8.05 cm; (<b>e</b>) Mode 1e, <span class="html-italic">R</span> = 6.55 cm; (<b>f</b>) Mode 1f, <span class="html-italic">R</span> = 6.15 cm; (<b>g</b>) Mode 1g, <span class="html-italic">R</span> = 6.80 cm; (<b>h</b>) Mode 1h, <span class="html-italic">R</span> = 5.60 cm.</p>
Full article ">Figure 4
<p>Spatial intensity distributions of different modes polarized along <span class="html-italic">y</span>-axis for selected bending radii <span class="html-italic">R</span>: (<b>a</b>) Mode 2a, <span class="html-italic">R</span> = 6.00 cm; (<b>b</b>) Mode 2b, <span class="html-italic">R</span> = 5.90 cm; (<b>c</b>) Mode 2c, <span class="html-italic">R</span> = 5.81 cm; (<b>d</b>) Mode 2d, <span class="html-italic">R</span> = 8.05 cm; (<b>e</b>) Mode 2e, <span class="html-italic">R</span> = 6.50 cm; (<b>f</b>) Mode 2f, <span class="html-italic">R</span> = 6.30 cm; (<b>g</b>) Mode 2g, <span class="html-italic">R</span> = 6.70 cm; (<b>h</b>) Mode 2h, <span class="html-italic">R</span> = 5.55 cm.</p>
Full article ">Figure 5
<p>(<b>a</b>) Dependences of relative integral intensities of Modes 1a–h on bending radius of MOF-18; (<b>b</b>) dependences of relative integral intensities of Modes 2a–h on bending radius of MOF-18.</p>
Full article ">Figure 6
<p>(<b>a</b>) Dependences of effective refractive indices of MOF-18 Modes 1a–h on bending radius <span class="html-italic">R</span>; (<b>b</b>) dependences of effective refractive indices of MOF-18 Modes 2a–h on bending radius <span class="html-italic">R</span>.</p>
Full article ">Figure 7
<p>(<b>a</b>) Differences in effective refractive index for different MOF-18 mode pairs polarized along <span class="html-italic">x</span>-axis versus bending radius <span class="html-italic">R</span>; (<b>b</b>) differences in effective refractive index for different MOF-18 mode pairs polarized along <span class="html-italic">y</span>-axis versus bending radius <span class="html-italic">R</span>.</p>
Full article ">Figure 8
<p>Spatial intensity distributions of Mode 2b for different bending radii: (<b>a</b>) 5.77 cm; (<b>b</b>) 5.82 cm; (<b>c</b>) 5.87 cm; spatial intensity distributions of Mode 2c for different bending radii: (<b>d</b>) 5.77 cm; (<b>e</b>) 5.82 cm; (<b>f</b>) 5.87 cm.</p>
Full article ">Figure 9
<p>Spatial distributions of electric field components <span class="html-italic">E</span><sub>y</sub> of Mode 2b for different bending radii: (<b>a</b>) 5.77 cm; (<b>b</b>) 5.82 cm; (<b>c</b>) 5.87 cm; spatial distributions of electric field components <span class="html-italic">E</span><sub>y</sub> of Mode 2c for different bending radii: (<b>d</b>) 5.77 cm; (<b>e</b>) 5.82 cm; (<b>f</b>) 5.87 cm.</p>
Full article ">Figure 9 Cont.
<p>Spatial distributions of electric field components <span class="html-italic">E</span><sub>y</sub> of Mode 2b for different bending radii: (<b>a</b>) 5.77 cm; (<b>b</b>) 5.82 cm; (<b>c</b>) 5.87 cm; spatial distributions of electric field components <span class="html-italic">E</span><sub>y</sub> of Mode 2c for different bending radii: (<b>d</b>) 5.77 cm; (<b>e</b>) 5.82 cm; (<b>f</b>) 5.87 cm.</p>
Full article ">Figure 10
<p>Spatial distributions of electric field components <span class="html-italic">E</span><sub>x</sub> of Mode 1d for different bending radii: (<b>a</b>) 7.97 cm; (<b>b</b>) 8.07 cm; (<b>c</b>) 8.17 cm.</p>
Full article ">Figure 11
<p>Schematic division of the MOF-18 cross-section into different regions: core (cor), ring gap (zaz), and outer silica cladding (cla).</p>
Full article ">Figure 12
<p>Relative integral intensities of Modes 1a (<b>a</b>), 1b (<b>b</b>), and 1c (<b>c</b>) in core (<span class="html-italic">I</span><sub>cor</sub>), ring gap (<span class="html-italic">I</span><sub>zaz</sub>), and cladding (<span class="html-italic">I</span><sub>cla</sub>) as a function of bending radius.</p>
Full article ">Figure 12 Cont.
<p>Relative integral intensities of Modes 1a (<b>a</b>), 1b (<b>b</b>), and 1c (<b>c</b>) in core (<span class="html-italic">I</span><sub>cor</sub>), ring gap (<span class="html-italic">I</span><sub>zaz</sub>), and cladding (<span class="html-italic">I</span><sub>cla</sub>) as a function of bending radius.</p>
Full article ">Figure 13
<p>(<b>a</b>) Relative values of overlap integral of the electric field components <span class="html-italic">E</span><sub>y</sub> of Mode 2b and 2c in core (cor), ring gap (zaz), and total (sum) as a function of bending radius; (<b>b</b>) relative values of overlap integral of electric field components <span class="html-italic">E</span><sub>x</sub> of Mode 1a and 1d in core (cor), ring gap (zaz), and total (sum) as a function of bending radius.</p>
Full article ">Figure 14
<p>(<b>a</b>) Leakage loss dependences of Modes 1a, 1b, and 1c on bending radius as well as final loss α<sub>1</sub> for MOF-18 with lengths <span class="html-italic">L</span> = 2 m; (<b>b</b>) leakage loss dependences of Modes 2a, 2b, and 2c on bending radius as well as final loss α<sub>2</sub> for MOF-18 with lengths <span class="html-italic">L</span> = 2 m.</p>
Full article ">Figure 15
<p>MOF-18 leakage loss dependences on bending radius for radiation polarized along <span class="html-italic">x</span>-axis (α<sub>1</sub>), along <span class="html-italic">y</span>-axis (α<sub>2</sub>), and for unpolarized radiation (α).</p>
Full article ">
14 pages, 3964 KiB  
Article
A High-Sensitivity Fiber Optic Soil Moisture Sensor Based on D-Shaped Fiber and Tin Oxide Thin Film Coatings
by Chuen-Lin Tien, Hsi-Fu Shih, Jia-Kai Tien and Ching-Chiun Wang
Sensors 2024, 24(23), 7474; https://doi.org/10.3390/s24237474 - 23 Nov 2024
Viewed by 692
Abstract
We present a high-sensitivity fiber optic soil moisture sensor based on side-polished multimode fibers and lossy mode resonance (LMR). The multimode fibers (MMFs), after side-polishing to form a D-shaped structure, are coated with a single-layer SnO2 thin film by electron beam evaporation [...] Read more.
We present a high-sensitivity fiber optic soil moisture sensor based on side-polished multimode fibers and lossy mode resonance (LMR). The multimode fibers (MMFs), after side-polishing to form a D-shaped structure, are coated with a single-layer SnO2 thin film by electron beam evaporation with ion-assisted deposition technology. The LMR effect can be obtained when the refractive index of the thin film is positive and greater than its extinction coefficient and the real part of the external medium permittivity. The D-shaped fiber optic soil moisture sensor was placed in soil, allowing moisture to penetrate into the thin film microstructure, and it observed the resonance wavelength shift in LMR spectra to measure the relative humidity change in soil. Meanwhile, an Arduino electronic soil moisture sensing module was used as the experimental control group, with soil relative humidity ranging from 10%RH to 90%RH. We found that the D-shaped fiber with a residual thickness of 93 μm and SnO2 thin film thickness of 450 nm had a maximum sensitivity of 2.29 nm/%RH, with relative humidity varying from 10%RH to 90%RH. The D-shaped fiber also demonstrates a fast response time and good reproducibility. Full article
(This article belongs to the Special Issue Imaging and Sensing in Optics and Photonics)
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Figure 1

Figure 1
<p>Schematic diagram of D-shaped multimode fiber structure.</p>
Full article ">Figure 2
<p>Microscopy image of D-shaped multimode optical fiber after side-polishing.</p>
Full article ">Figure 3
<p>Schematic diagram of LMR phase-matching condition.</p>
Full article ">Figure 4
<p>The proposed D-shaped MMF coated with a SnO<sub>2</sub> thin film.</p>
Full article ">Figure 5
<p>Cross-sectional view of SEM image of SnO<sub>2</sub> thin film.</p>
Full article ">Figure 6
<p>Experimental setup of fiber soil moisture sensor.</p>
Full article ">Figure 7
<p>Spectra of soil moisture sensor with single-layer SnO<sub>2</sub> thin film.</p>
Full article ">Figure 8
<p>Linear fitting of sensitivity of single-layer SnO<sub>2</sub> film coated on D-shaped fiber.</p>
Full article ">Figure 9
<p>A plot of the resonant wavelength of the LMR sensor as a function of time as soil moisture changes from 10% to 90%RH. The pink line is the measured data and the grey line marks the response time.</p>
Full article ">Figure 10
<p>The response time of the LMR sensor to soil moisture switching from 10% RH to 50% RH under five soil moisture cycles. The red line is the measurement data, the purple line represents the 1150 nm scale, and the gray line represents the response time.</p>
Full article ">
24 pages, 12773 KiB  
Article
Anticrossing and Mode Coupling in Bent All-Glass Leakage Channel Microstructured Optical Fibers with Large Mode Area
by Alexander N. Denisov, Vladislav V. Dvoyrin and Sergey L. Semjonov
Photonics 2024, 11(10), 985; https://doi.org/10.3390/photonics11100985 - 19 Oct 2024
Viewed by 655
Abstract
This paper presents the results of a detailed theoretical study of the bending properties of original all-glass leakage channel microstructured optical fibers (LC MOFs) over a bending radius range from 3 cm to 11 cm. These LC MOFs contain two layers of fluorine-doped [...] Read more.
This paper presents the results of a detailed theoretical study of the bending properties of original all-glass leakage channel microstructured optical fibers (LC MOFs) over a bending radius range from 3 cm to 11 cm. These LC MOFs contain two layers of fluorine-doped silica glass elements with reduced refractive index, different diameters, and different distances between them. We determined the spatial distributions of the electric field components of different modes in addition to the usual parameters such as effective refractive indices, bending losses, and spatial intensity distributions. A detailed analysis showed that three modes for each polarization have to be considered to correctly calculate the bending losses. Two pairs of these three modes couple in two distinct bending radius ranges, specifically near 3.68 cm and near 5.95 cm, and the mode coupling in these pairs is resonant. The resulting bending losses of the LC MOF for two polarizations are very close to each other and have two maxima at bending radii of 3.68 cm and 5.95 cm. However, the nature of these maxima is not resonant; they are caused by the combined influence of all three modes, each of which has specific dependencies of losses and other parameters on the bending radius that exhibit quasi-resonant behavior near the corresponding bending radii. Full article
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Figure 1

Figure 1
<p>Structure of MOF-18: <span class="html-italic">d</span><sub>1</sub>/Λ<sub>1</sub> = 0.82; <span class="html-italic">d</span><sub>2</sub>/<span class="html-italic">d</span><sub>1</sub> = 1.25; <span class="html-italic">d</span><sub>3</sub>/<span class="html-italic">d</span><sub>1</sub> = 0.90; Λ<sub>2</sub>/Λ<sub>1</sub> = 1.25; and Λ<sub>3</sub>/Λ<sub>1</sub> = 1.10.</p>
Full article ">Figure 2
<p>Spatial distribution of <span class="html-italic">n</span><sub>equ</sub> across the MOF-18 cross section for <span class="html-italic">R</span> = 0.03 m.</p>
Full article ">Figure 3
<p>Dependences of the effective refractive indices of MOF-18 Modes 1a, 1b, and 1c on the bending radius <span class="html-italic">R</span>. Insets—spatial intensity distributions of Modes 1a, 1b, and 1c for bending radii of 3.0 cm, 5.0 cm, and 7.0 cm; red arrows indicate direction and relative magnitude of electric field.</p>
Full article ">Figure 4
<p>Differences in effective refractive index for different pairs of orthogonal modes of MOF-18 as a function of bending radius <span class="html-italic">R</span>.</p>
Full article ">Figure 5
<p>(<b>a</b>) Spatial intensity distributions of Modes 1a and 1b for bending radii from 5.70 cm to 6.25 cm; (<b>b</b>) spatial intensity distributions of Modes 1b and 1c for bending radii from 3.50 cm to 3.90 cm.</p>
Full article ">Figure 5 Cont.
<p>(<b>a</b>) Spatial intensity distributions of Modes 1a and 1b for bending radii from 5.70 cm to 6.25 cm; (<b>b</b>) spatial intensity distributions of Modes 1b and 1c for bending radii from 3.50 cm to 3.90 cm.</p>
Full article ">Figure 6
<p>Differences in effective refractive index for different MOF-18 mode pairs versus bending radius <span class="html-italic">R</span>.</p>
Full article ">Figure 7
<p>Spatial distributions of the electric field components <span class="html-italic">E</span><sub>x</sub> of Modes 1a and 1b for bending radii of 5.70 cm (<b>a</b>), 5.85 cm (<b>b</b>), 5.95 cm (<b>c</b>), 6.10 cm (<b>d</b>), and 6.25 cm (<b>e</b>).</p>
Full article ">Figure 8
<p>Spatial distributions of the electric field components <span class="html-italic">E</span><sub>x</sub> of Mode 1b for bending radii of 4.10 cm (<b>a</b>), 4.50 cm (<b>b</b>), 4.90 cm (<b>c</b>), 5.30 cm (<b>d</b>), 5.50 cm (<b>e</b>), and 5.60 cm (<b>f</b>).</p>
Full article ">Figure 9
<p>Schematic division of the MOF-18 cross section into different regions: core (cor), ring gap (zaz), and cladding (cla).</p>
Full article ">Figure 10
<p>(<b>a</b>) Relative intensities of Modes 1a and 1b in the core (<span class="html-italic">I</span><sub>1a_cor</sub> and <span class="html-italic">I</span><sub>1b_cor</sub>), in the ring gap (<span class="html-italic">I</span><sub>1a_zaz</sub> and <span class="html-italic">I</span><sub>1b_zaz</sub>), and in the cladding (<span class="html-italic">I</span><sub>1a_cla</sub> and <span class="html-italic">I</span><sub>1b_cla</sub>) as a function of the bending radius; (<b>b</b>) dependencies of Modes 1a and 1b leakage losses (α<sub>1a</sub> and α<sub>1b</sub>) and the relative intensities in the cladding (<span class="html-italic">I</span><sub>1a_cla</sub> and <span class="html-italic">I</span><sub>1b_cla</sub>) on the bending radius.</p>
Full article ">Figure 11
<p>(<b>a</b>) Dependences of the leakage losses (α<sub>1a</sub>, α<sub>1b</sub>, and α<sub>1c</sub>) of Modes 1a, 1b, and 1c on the bending radius of MOF-18; (<b>b</b>) dependences of the relative intensities (<span class="html-italic">I</span><sub>01a</sub>, <span class="html-italic">I</span><sub>01b</sub>, and <span class="html-italic">I</span><sub>01c</sub>) of Modes 1a, 1b, and 1c on the bending radius of MOF-18.</p>
Full article ">Figure 12
<p>(<b>a</b>) Leakage loss dependences of Modes 1a, 1b, and 1c on MOF-18 bending radius as well as final loss α<sub>1</sub> for MOF-18 with lengths <span class="html-italic">L</span> = 10 m and <span class="html-italic">L</span> = 2 m; (<b>b</b>) MOF-18 leakage loss dependences on bending radius for radiation polarized along <span class="html-italic">x</span>-axis (α<sub>1</sub>) and <span class="html-italic">y</span>-axis (α<sub>2</sub>).</p>
Full article ">Figure A1
<p>Spatial distributions of the electric field components <span class="html-italic">E</span><sub>x</sub> of Modes 1b and 1c for bending radii of 3.50 cm (<b>a</b>), 3.60 cm (<b>b</b>), 3.68 cm (<b>c</b>), 3.80 cm (<b>d</b>), and 3.90 cm (<b>e</b>).</p>
Full article ">Figure A1 Cont.
<p>Spatial distributions of the electric field components <span class="html-italic">E</span><sub>x</sub> of Modes 1b and 1c for bending radii of 3.50 cm (<b>a</b>), 3.60 cm (<b>b</b>), 3.68 cm (<b>c</b>), 3.80 cm (<b>d</b>), and 3.90 cm (<b>e</b>).</p>
Full article ">Figure A2
<p>(<b>a</b>) Relative intensities of Modes 1b and 1c in the core (<span class="html-italic">I</span><sub>1b_cor</sub> and <span class="html-italic">I</span><sub>1c_cor</sub>), in the ring gap (<span class="html-italic">I</span><sub>1b_zaz</sub> and <span class="html-italic">I</span><sub>1c_zaz</sub>), and in the cladding (<span class="html-italic">I</span><sub>1b_cla</sub> and <span class="html-italic">I</span><sub>1c_cla</sub>) as a function of the bending radius; (<b>b</b>) dependencies of Modes 1b and 1c leakage losses (α<sub>1b</sub> and α<sub>1c</sub>) and the relative intensities in the cladding (<span class="html-italic">I</span><sub>1b_cla</sub> and <span class="html-italic">I</span><sub>1c_cla</sub>) on the bending radius.</p>
Full article ">Figure A2 Cont.
<p>(<b>a</b>) Relative intensities of Modes 1b and 1c in the core (<span class="html-italic">I</span><sub>1b_cor</sub> and <span class="html-italic">I</span><sub>1c_cor</sub>), in the ring gap (<span class="html-italic">I</span><sub>1b_zaz</sub> and <span class="html-italic">I</span><sub>1c_zaz</sub>), and in the cladding (<span class="html-italic">I</span><sub>1b_cla</sub> and <span class="html-italic">I</span><sub>1c_cla</sub>) as a function of the bending radius; (<b>b</b>) dependencies of Modes 1b and 1c leakage losses (α<sub>1b</sub> and α<sub>1c</sub>) and the relative intensities in the cladding (<span class="html-italic">I</span><sub>1b_cla</sub> and <span class="html-italic">I</span><sub>1c_cla</sub>) on the bending radius.</p>
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15 pages, 6969 KiB  
Article
Effects of Continuous Rolling and Reversible Rolling on 2.4% Si Non-Oriented Silicon Steel
by Kaixuan Shao, Yuhao Niu, Yinghao Pei, Jialong Qiao, Hongbo Pan and Haijun Wang
Crystals 2024, 14(9), 824; https://doi.org/10.3390/cryst14090824 - 20 Sep 2024
Viewed by 738
Abstract
The cold-rolled non-oriented silicon steel sheets with a Si content of 2.4 wt.%, produced by continuous and reversible cold rolling, were used as the experimental material. The effects of annealing temperature on the microstructure, texture, and magnetic properties were studied by optical microscopy, [...] Read more.
The cold-rolled non-oriented silicon steel sheets with a Si content of 2.4 wt.%, produced by continuous and reversible cold rolling, were used as the experimental material. The effects of annealing temperature on the microstructure, texture, and magnetic properties were studied by optical microscopy, an X-ray diffractometer, and a magnetic property measuring instrument. The experimental results showed that the dominant texture components at the surface of both sheets were almost the same, i.e., α and γ fibers. After annealing at 920 °C for 30 s, a complete recrystallization occurred in both sheets. When annealing below 1070 °C, the average grain sizes of continuous cold-rolled sheets were slightly higher than those of reversible cold-rolled ones. Additionally, for all specimens, the recrystallization texture components were γ fiber, as well as weak α fiber, λ fiber, and Goss texture. Additionally, the difference was the texture intensity. The iron losses of the finished products of continuous cold rolling were lower than those of the finished products of reversible cold rolling with the increase in annealing temperature, and the magnetic induction was higher than that of the finished products of reversible cold rolling. Full article
(This article belongs to the Special Issue Crystallization of High Performance Metallic Materials (2nd Edition))
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<p>Laboratory annealing process diagram.</p>
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<p>Textures in the surface layer of hot-rolled and normalized sheets. (<b>a</b>) Hot-rolled sheet and (<b>b</b>) normalized sheet. The numbers in the figures are texture intensities.</p>
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<p>Microstructures of continuous cold-rolled sheet and reversible cold-rolled sheet. (<b>a</b>) Continuous cold-rolled sheet and (<b>b</b>) reversible cold-rolled sheet.</p>
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<p>Surface textures of continuous cold-rolled sheet and reversible cold-rolled sheet. (<b>a</b>) Continuous cold-rolled sheet and (<b>b</b>) reversible cold-rolled sheet.</p>
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<p>Microstructures of annealed sheets. (<b>a1</b>–<b>f1</b>) annealed sheets with continuous cold rolling; (<b>a2</b>–<b>f2</b>) annealed sheet with reversible cold rolling; (<b>a1</b>,<b>a2</b>) 920 °C; (<b>b1</b>,<b>b2</b>) 950 °C; (<b>c1</b>,<b>c2</b>) 980 °C; (<b>d1</b>,<b>d2</b>) 1010 °C; (<b>e1</b>,<b>e2</b>) 1040 °C; and (<b>f1</b>,<b>f2</b>) 1070 °C.</p>
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<p>Average grain size of annealed sheets at different temperatures.</p>
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<p>Iron losses P<sub>1.5/50</sub> and magnetic induction B<sub>50</sub> of 2.4%Si non-oriented silicon steel after different annealing temperatures.</p>
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<p>Simplified schematic diagram of rolling deformation and stress of polycrystalline sheet.</p>
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<p>The density changes of α and γ fibers under different reduction rates. (<b>a</b>) The density changes of α fiber and (<b>b</b>) the density changes of γ fiber.</p>
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<p>α and γ fibers of continuous cold-rolled sheets after different annealing temperatures. (<b>a</b>) α fiber of continuous cold-rolled sheets and (<b>b</b>) γ fiber of continuous cold-rolled sheets.</p>
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<p>α and γ fibers of reversible cold-rolled sheets after different annealing temperatures. (<b>a</b>) α fiber of reversible cold-rolled sheets and (<b>b</b>) γ fiber of reversible cold-rolled sheets.</p>
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<p>The average grain size and iron losses at different annealing temperatures.</p>
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11 pages, 2601 KiB  
Article
Neural Network Approach for Modelling and Compensation of Local Surface-Tilting-Dependent Topography Measurement Errors in Coherence Scanning Interferometry
by Sai Gao, Zhi Li and Uwe Brand
Metrology 2024, 4(3), 446-456; https://doi.org/10.3390/metrology4030027 - 9 Sep 2024
Viewed by 3286
Abstract
The topography measurement accuracy of coherence scanning interferometry (CSI) suffers from the local characteristic of micro-structured surfaces, such as local surface slopes. A cylindrical reference artefact made of single-mode fiber with high roundness and low roughness has been proposed in this manuscript to [...] Read more.
The topography measurement accuracy of coherence scanning interferometry (CSI) suffers from the local characteristic of micro-structured surfaces, such as local surface slopes. A cylindrical reference artefact made of single-mode fiber with high roundness and low roughness has been proposed in this manuscript to traceably investigate the surface tilting induced measurement deviations using coherence scanning interferometry with high NA objectives. A feed-forward neural network (FF-NN) is designed and trained to model and thereafter compensate the systematic measurement deviations due to local surface tilting. Experimental results have verified that the FF-NN approach can well enhance the accuracy of the CSI for radius measurement of cylindrical samples up to 0.3%. Further development of the FF-NN for modelling of the measurement errors in CSI due to the optical properties of surfaces including areal roughness is outlined. Full article
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<p>Schematic of ray tracing analysis of a Mirau interference microscope objective in imaging locally tilted surface.</p>
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<p>Cylindrical reference artefact used for evaluation of the topography measurement error of an interference microscope: (<b>a</b>) schematic of the cylinder artefact; (<b>b</b>) influence of the topography measurement errors on the estimation of cylinder radius.</p>
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<p>Traceable measurement of the topography of cylindrical reference artefacts using a MEMS-SPM; (<b>a</b>) Schematic diagram of the MEMS-SPM head for topography measurement; (<b>b</b>) Schematic of the topography measurement on micro-cylinder using an AFM probe; (<b>c</b>) photography of the MEMS-SPM head mounted on a PCB; (<b>d</b>) Sideview of an AFM probe clamped in the passive MEMS cantilever holder.</p>
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<p>Architecture of the neural network model used for modelling of the surface tilting induced topography measurement errors in an interference microscope.</p>
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<p>Surface topography of the reference cylindrical artefact measured by the MEMS-SPM: (<b>a</b>) 3D topography of the artefact; (<b>b</b>) Cross-sectional profile of the SM fiber at y = 51 µm and its roundness error.</p>
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<p>Surface topography of the reference cylindrical artefact measured by the CSI (<b>a</b>) 3D topography of the artefact; (<b>b</b>) Cross-sectional profile of the SM fiber at y = 160 µm and its roundness error.</p>
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<p>Evaluation and Modelling of topography measurement errors in a CSI microscope using a Mirau objective with NA = 0.55: (<b>a</b>) interference microscopic measurement error with respect to the reference topography measured by the MEMS-SPM; (<b>b</b>) approximation of the γ<sub>s</sub>-induced measure errors using a trained FF-NN with 15 neurons in its single HL; (<b>c</b>) Comparison of the compensation results using a feed-forward neural network with different neuron numbers in the single hidden layer (HL); (<b>d</b>) residuals with and without FF-NN compensation.</p>
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<p>Evaluation and Modelling of topography measurement errors in a CSI microscope using a Mirau objective with NA = 0.55: (<b>a</b>) interference microscopic measurement error with respect to the reference topography measured by the MEMS-SPM; (<b>b</b>) approximation of the γ<sub>s</sub>-induced measure errors using a trained FF-NN with 15 neurons in its single HL; (<b>c</b>) Comparison of the compensation results using a feed-forward neural network with different neuron numbers in the single hidden layer (HL); (<b>d</b>) residuals with and without FF-NN compensation.</p>
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14 pages, 4846 KiB  
Article
In-Fiber Hybrid Structure Sensor Based on the Vernier Effect for Vector Curvature and Temperature Measurement
by Sunde Wang, Tiantong Zhao, Baoqun Li, Silun Du, Deqi Li, Dongmei Liu and Tianshu Wang
Photonics 2024, 11(8), 703; https://doi.org/10.3390/photonics11080703 - 28 Jul 2024
Viewed by 1000
Abstract
A vector curvature and temperature sensor based on an in-fiber hybrid microstructure is proposed and experimentally demonstrated. The proposed scheme enables the dimensions of the Fabry–Perot and Mach–Zehnder hybrid interferometer to be adjusted for the formation of the Vernier effect by simply changing [...] Read more.
A vector curvature and temperature sensor based on an in-fiber hybrid microstructure is proposed and experimentally demonstrated. The proposed scheme enables the dimensions of the Fabry–Perot and Mach–Zehnder hybrid interferometer to be adjusted for the formation of the Vernier effect by simply changing the length of a single optical fiber. The sensor is fabricated using a fiber Bragg grating (FBG), multimode fiber (MMF), and a single-hole dual-core fiber (SHDCF). The sensor exhibits different curvature sensitivities in four vertical directions, enabling two-dimensional curvature sensing. The temperature and curvature sensitivities of the sensor were enhanced to 100 pm/°C and −25.55 nm/m−1, respectively, and the temperature crosstalk was minimal at −3.9 × 10−3 m−1/°C. This hybrid microstructure sensor technology can be applied to high-sensitivity two-dimensional vector curvature and temperature detection for structural health monitoring of buildings, bridge engineering, and other related fields. Full article
(This article belongs to the Section Lasers, Light Sources and Sensors)
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<p>(<b>a</b>) Structure diagram of the sensor. (<b>b</b>) The cross-section of the SHDCF.</p>
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<p>(<b>a</b>) Energy distribution in multimode fiber. (<b>b</b>) Energy distribution in the PAHM structure.</p>
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<p>(<b>a</b>) Transmission spectra of the PAHM sensor under different SHDCF lengths. (<b>b</b>) The spatial frequency spectrum of the PAHM sensor under different SHDCF lengths.</p>
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<p>Transmission spectrum of the FBG-PAHM structured sensor.</p>
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<p>Schematic diagram of the experimental system.</p>
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<p>The sensor structure’s response to curvature: (<b>a</b>) 0°, (<b>b</b>) 90°, (<b>c</b>) 180°, and (<b>d</b>) 270°.</p>
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<p>(<b>a</b>) At various rotational azimuth angles, as a function of dip wavelength-curvature. (<b>b</b>) Relationship between the resonant wavelength of FBG and curvature with curvature increasing.</p>
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<p>(<b>a</b>) The vector curve repeatability test characterization. (<b>b</b>) Sensor stability measurement for four hours.</p>
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<p>The wavelength shifts of the envelope and the FBG with the temperature change: (<b>a</b>) three-dimensional image, (<b>b</b>) two-dimensional image and a magnified view of the wavelength shift of the FBG resonance in the inset.</p>
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<p>Response of the sensor structure to the different temperatures.</p>
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12 pages, 3890 KiB  
Article
Side-Opened Hollow Fiber-Based SPR Sensor for High Refractive Index Detection
by Ge Meng, Nannan Luan, Hao He, Fan Lei and Jianfei Liu
Sensors 2024, 24(13), 4335; https://doi.org/10.3390/s24134335 - 4 Jul 2024
Cited by 1 | Viewed by 992
Abstract
To facilitate the sensor fabrication and sensing operation in microstructured optical fiber-based surface plasmon resonance (SPR) sensors for high refractive index (RI) detection, we propose a special hollow fiber-based SPR sensor that comprises an opening on its body side and a thin gold [...] Read more.
To facilitate the sensor fabrication and sensing operation in microstructured optical fiber-based surface plasmon resonance (SPR) sensors for high refractive index (RI) detection, we propose a special hollow fiber-based SPR sensor that comprises an opening on its body side and a thin gold layer coated on its outer surface. The analyte is able to flow into the hollow core through the side-opening to form new fiber core, with the Gaussian-like mode propagating in it. We investigate the sensing performance of the proposed sensor in a higher RI range of 1.48 to 1.54 at two feasible schemes: one is to only fill the fiber core with analyte (Scheme A), and the other is to directly immerse the sensor in the analyte (Scheme B). The results demonstrate that our sensor exhibits higher wavelength sensitivity at Scheme A with a maximum wavelength sensitivity of 12,320 nm/RIU, while a greater amplitude sensitivity was found at Scheme B with a maximum amplitude sensitivity of 1146 RIU−1. Our proposed sensor features the advantages of simple fabrication, flexible operation, easy analyte filling and replacing, enhanced real-time detection capabilities, high RI detection, and very high wavelength sensitivity and amplitude sensitivity, which makes it more competitive in SPR sensing applications. Full article
(This article belongs to the Collection Optical Fiber Sensors)
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<p>Schematics of the side-opened HF-based SPR sensor. (<b>a</b>) 3D-view and the experimental setup of the sensor for high RI detection. (<b>b</b>) Cross-section view of Scheme A which is to only fill the hollow core with analyte. (<b>c</b>) Cross-section view of Scheme B which is to immerse the sensor in analyte.</p>
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<p>Dispersion relations of the core-guided mode and the plasmonic mode of the proposed sensor at (<b>a</b>) Scheme A and (<b>b</b>) Scheme B when the <span class="html-italic">n</span><sub>a</sub> changes from 1.49 to 1.50. Insets show the evolution of electric field distributions of the corresponding modes. Loss spectra of the core-guided mode of the sensor at (<b>c</b>) Scheme A and (<b>d</b>) Scheme B when the <span class="html-italic">n</span><sub>a</sub> changes from 1.49 to 1.50. For comparison, the blue dash-dotted lines show the losses of the core-guided mode without gold coating at <span class="html-italic">n</span><sub>a</sub> = 1.49.</p>
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<p>Resonance wavelengths and peak losses of the sensor with different <span class="html-italic">n</span><sub>a</sub> at (<b>a</b>) Scheme A and (<b>b</b>) Scheme B. (<b>c</b>) Wavelength sensitivities of the sensor with different <span class="html-italic">n</span><sub>a</sub> at the two schemes.</p>
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<p>Amplitude sensitivities of the sensor under different <span class="html-italic">n</span><sub>a</sub> at (<b>a</b>) Scheme A and (<b>b</b>) Scheme B. (<b>c</b>) Comparison of the maximum amplitude sensitivity under different <span class="html-italic">n</span><sub>a</sub> at the two schemes.</p>
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<p>Loss spectra of the core-guided mode of the sensor with <span class="html-italic">n</span><sub>a</sub> = 1.48 under different <span class="html-italic">w</span> at (<b>a</b>) Scheme A and (<b>b</b>) Scheme B. (<b>c</b>) The electric field distribution of the core-guided mode of the sensor with <span class="html-italic">n</span><sub>a</sub> = 1.48 under different <span class="html-italic">w</span> at their respective resonance wavelengths.</p>
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<p>Variations of wavelength sensitivities of the sensor with <span class="html-italic">n</span><sub>a</sub> changing under different <span class="html-italic">w</span> at (<b>a</b>) Scheme A and (<b>b</b>) Scheme B.</p>
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<p>Variations of the maximum amplitude sensitivities of the sensor with <span class="html-italic">n</span><sub>a</sub> changing under different <span class="html-italic">w</span> at (<b>a</b>) Scheme A and (<b>b</b>) Scheme B.</p>
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9 pages, 2326 KiB  
Article
A Novel Small Form-Factor Handheld Optical Coherence Tomography Probe for Oral Soft Tissue Imaging
by Alok K. Kushwaha, Minqi Ji, Sneha Sethi, Lisa Jamieson, Robert A. McLaughlin and Jiawen Li
Micromachines 2024, 15(6), 742; https://doi.org/10.3390/mi15060742 - 31 May 2024
Viewed by 1070
Abstract
Tissue imaging is crucial in oral cancer diagnostics. Imaging techniques such as X-ray imaging, magnetic resonance imaging, optical coherence tomography (OCT) and computed tomography (CT) enable the visualization and analysis of tissues, aiding in the detection and diagnosis of cancers. A significant amount [...] Read more.
Tissue imaging is crucial in oral cancer diagnostics. Imaging techniques such as X-ray imaging, magnetic resonance imaging, optical coherence tomography (OCT) and computed tomography (CT) enable the visualization and analysis of tissues, aiding in the detection and diagnosis of cancers. A significant amount of research has been conducted on designing OCT probes for tissue imaging, but most probes are either heavy, bulky and require external mounting or are lightweight but straight. This study addresses these challenges, resulting in a curved lightweight, low-voltage and compact handheld imaging probe for oral soft tissue examination. To the best of our knowledge, this is the first curved handheld OCT probe with its shape optimized for oral applications. This probe features highly compact all-fiber optics with a diameter of 125 μm and utilizes innovative central deflection magnetic actuation for controlled beam scanning. To ensure vertical stability while scanning oral soft tissues, the fiber was secured through multiple narrow slits at the probe’s distal end. This apparatus was encased in a 3D-printed angular cylinder tube (15 mm outer diameter, 12 mm inner diameter and 160 mm in length, weighing < 20 g). An angle of 115° makes the probe easy to hold and suitable for scanning in space-limited locations. To validate the feasibility of this probe, we conducted assessments on a multi-layered imaging phantom and human tissues, visualizing microstructural features with high contrast. Full article
(This article belongs to the Special Issue Optical Coherence Tomography (OCT) Technique and Its Applications)
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<p>(<b>a</b>) Diagram of a handheld angular probe (isometric view) and (<b>b</b>) the in vivo application of the curved handheld probe in a human oral cavity (labial mucosa).</p>
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<p>The handheld angular probe interfaced to the microcontroller and OCT system. The black color is used for electrical signals (e.g., a 3 V peak-to-peak sinusoidal signal is generated from the microcontroller to produce a magnetic field strong enough to deflect lensed fiber) and the orange color is used for optical signals (e.g., near-infrared light from the OCT system directed towards the oral soft tissue).</p>
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<p>Dimensions inside the probe at the distal end. The distal end of the probe has a window slot (12 mm diameter and a groove with 1 mm depth) for the sapphire glass (8 mm diameter and 0.15 mm thickness).</p>
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<p>(<b>a</b>) The coil (diameter: 0.25 mm; number of turns: 60) mounted on a 3D-printed structure of 10 mm outer diameter and 4.5 mm internal diameter, (<b>b</b>) the deflection unit with two holes with a diameter of 500 μm to pass through the lensed fiber with a diameter of 125 μm, (<b>c</b>) the deflection unit with a magnet and (<b>d</b>) the assembly of the deflection unit, the magnet, the flexible strip, the lensed fiber and the coil.</p>
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<p>(<b>a</b>) Image of a sticky tape phantom object, which has more than 15 layers of sticky tape. (<b>b</b>,<b>c</b>) In vivo OCT cross-section of the normal human oral soft tissue. C: connective tissue; EP: epithelium; G: glandular structures; M: micro-vessels; S: sapphire glass cover.</p>
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16 pages, 8559 KiB  
Article
Microstructure and Texture Evolution in Cold-Rolled and Annealed Oxygen-Free Copper Sheets
by Jing Qin, Xun Li, Dongsheng Wang, Chen Zhou, Tongsheng Hu, Jingwen Wang, Youwen Yang and Yujun Hu
Materials 2024, 17(10), 2202; https://doi.org/10.3390/ma17102202 - 8 May 2024
Viewed by 1331
Abstract
Commercial oxygen-free copper sheets were cold-rolled with reduction rates ranging from 20% to 87% and annealed at 400, 500 and 600 °C. The microstructure and texture evolution during the cold-rolling and annealing processes were studied using optical microscopy (OM), scanning electron microscopy (SEM) [...] Read more.
Commercial oxygen-free copper sheets were cold-rolled with reduction rates ranging from 20% to 87% and annealed at 400, 500 and 600 °C. The microstructure and texture evolution during the cold-rolling and annealing processes were studied using optical microscopy (OM), scanning electron microscopy (SEM) and electron back-scattered diffraction (EBSD). The results show that the deformation textures of {123}<634> (S), {112}<111> (Copper) and {110}<112> (Brass) were continuously enhanced with the increase in cold-rolling reduction. The orientations along the α-oriented fiber converged towards Brass, and the orientation density of β fiber obviously increased when the rolling reduction exceeded 60%. The recrystallization texture was significantly affected by the cold-rolling reduction. After 60% cold-rolling reduction, Copper and S texture components gradually decreased, and the {011}<511> recrystallization texture component formed with the increase in annealing temperature. After 87% cold-rolling reduction, a strong Cube texture formed, and other textures were inhibited with the increase in annealing temperature. The strong Brass and S deformation texture was conducive to the formation of a strong Cube annealing texture. The density of the annealing twin boundary decreased with the increase in annealing temperature, and more annealing twin boundaries formed in the oxygen-free copper sheets with the increase in cold-rolling reduction. Full article
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<p>Metallographic microstructure of copper sheets under different rolling reductions: (<b>a</b>) 0; (<b>b</b>) 20%; (<b>c</b>) 40%; (<b>d</b>) 60%; (<b>e</b>) 80% and (<b>f</b>) 87%.</p>
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<p>IPF maps of copper sheets under different rolling reductions: (<b>a</b>) 0; (<b>b</b>) 20%; (<b>c</b>) 40%; (<b>d</b>) 60%; (<b>e</b>) 80% and (<b>f</b>) 87%.</p>
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<p>ODF maps at φ<sub>2</sub> = 0°, 45° and 65° (levels: 1, 2, 3, 4 …) under different rolling reductions: (<b>a</b>) 0; (<b>b</b>) 20%; (<b>c</b>) 40%; (<b>d</b>) 60%; (<b>e</b>) 80% and (<b>f</b>) 87%.</p>
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<p>Volume fractions of main deformation texture components (<b>a</b>), variation curves of orientation densities along α-fiber (<b>b</b>) and β-fiber (<b>c</b>) under different rolling reductions.</p>
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<p>Metallographic microstructure of copper sheets with different rolling reduction rates and annealing temperatures: (<b>a</b>) 60%, 400 °C; (<b>b</b>) 87%, 400 °C; (<b>c</b>) 60%, 500 °C; (<b>d</b>) 87%, 500 °C; (<b>e</b>) 60%, 600 °C and (<b>f</b>) 87%, 600 °C.</p>
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<p>IPF maps of copper sheets with different rolling reduction rates and annealing temperatures: (<b>a</b>) 60%, 400 °C; (<b>b</b>) 87%, 400 °C; (<b>c</b>) 60%, 500 °C; (<b>d</b>) 87%, 500 °C; (<b>e</b>) 60%, 600 °C and (<b>f</b>) 87%, 600 °C.</p>
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<p>ODF maps at φ<sub>2</sub> = 0°, 45° and 65° (levels: 1, 2, 3, 4 …) of copper sheets with different rolling reduction rates and annealing temperatures: (<b>a</b>) 60%, 400°C; (<b>b</b>) 60%, 500 °C; (<b>c</b>) 60%, 600 °C; (<b>d</b>) 87%, 400 °C; (<b>e</b>) 87%, 500 °C and (<b>f</b>) 87%, 600 °C.</p>
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<p>Maps of main texture components in copper sheets with different rolling reduction rates and annealing temperatures: (<b>a</b>) 60%, 400 °C; (<b>b</b>) 87%, 400 °C; (<b>c</b>) 60%, 500 °C; (<b>d</b>) 87%, 500 °C; (<b>e</b>) 60%, 600 °C and (<b>f</b>) 87%, 600 °C.</p>
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<p>Volume fractions of main texture components in annealed copper sheets with different rolling reduction rates: (<b>a</b>) 60% and (<b>b</b>) 87%.</p>
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<p>Distribution and density of twins in copper sheets with different rolling reduction rates and annealing temperatures: (<b>a</b>) 60%, As-rolled; (<b>b</b>) 87%, As-rolled; (<b>c</b>) 60%, 400 °C; (<b>d</b>) 87%, 400 °C; (<b>e</b>) 60%, 500 °C; (<b>f</b>) 87%, 500 °C; (<b>g</b>) 60%, 600 °C and (<b>h</b>) 87%, 600 °C.</p>
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<p>Grain boundary characteristics of copper sheets with different rolling reduction rates: (<b>a</b>) 60% and (<b>b</b>) 87%.</p>
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<p>Typical region with many annealing twins selected in <a href="#materials-17-02202-f008" class="html-fig">Figure 8</a>d: (<b>a</b>) main texture components and their 3D crystal Cube with Euler angles; (<b>b</b>) corresponding orientations in {111} pole figure; (<b>c</b>) misorientation angles along line 1; (<b>d</b>) misorientation angles along line 2 and (<b>e</b>) misorientation angles along line 3.</p>
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21 pages, 3957 KiB  
Article
Manufacture of Microstructured Optical Fibers: Problem of Optimal Control of Silica Capillary Drawing Process
by Daria Vladimirova, Vladimir Pervadchuk and Yuri Konstantinov
Computation 2024, 12(5), 86; https://doi.org/10.3390/computation12050086 - 23 Apr 2024
Cited by 1 | Viewed by 1269
Abstract
The effective control of any technological process is essential in ensuring high-quality finished products. This is particularly true in manufacturing knowledge-intensive and high-tech products, including microstructured photonic crystal fibers (PCF). This paper addresses the issues of stabilizing the optimal control of the silica [...] Read more.
The effective control of any technological process is essential in ensuring high-quality finished products. This is particularly true in manufacturing knowledge-intensive and high-tech products, including microstructured photonic crystal fibers (PCF). This paper addresses the issues of stabilizing the optimal control of the silica capillary drawing process. The silica capillaries are the main components of PCF. A modified mathematical model proposed by the authors is used as the basic model of capillary drawing. The uniqueness of this model is that it takes into account the main forces acting during drawing (gravity, inertia, viscosity, surface tension, pressure inside the drawn capillary), as well as all types of heat transfer (heat conduction, convection, radiation). In the first stage, the system of partial differential equations describing heat and mass transfer was linearized. Then, the problem of the optimal control of the drawing process was formulated, and optimization systems for the isothermal and non-isothermal cases were obtained. In the isothermal case, optimal adjustments of the drawing speed were obtained for different objective functionals. Thus, the proposed approach allows for the constant monitoring and adjustment of the observed state parameters (for example, the outer radius of the capillary). This is possible due to the optimal control of the drawing speed to obtain high-quality preforms. The ability to control and promptly eliminate geometric defects in the capillary was confirmed by the analysis of the numerical calculations, according to which even 15% deviations in the outer radius of the capillary during the drawing process can be reduced to 4–5% by controlling only the capillary drawing speed. Full article
(This article belongs to the Special Issue Mathematical Modeling and Study of Nonlinear Dynamic Processes)
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<p>Configuration of measurement area.</p>
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<p>Radiant heat transfer during capillary drawing.</p>
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<p>Dependence of the inner radius of the capillary on the feed and draw rates and the furnace temperature: curves 1, 2 (feed rate 2 × 10<sup>−3</sup> m/min), curves 3, 4 (feed rate 4 × 10<sup>−3</sup> m/min), curves 5, 6 (feed rate 8 × 10<sup>−3</sup> m/min); ▲ (experiment), solid line (calculated values according to the proposed model).</p>
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<p>Examples of typical surface defects in preforms (highlighted in red): (<b>a</b>) air bubbles, (<b>b</b>) streaks, (<b>c</b>) inclusions and contaminations, (<b>d</b>) top material lack.</p>
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<p>Calculated values of deviations in outer and inner radii in optimal control mode and without it, with optimal control function (in the case of the objective functional (15)): (<b>a</b>) regularization parameter (control cost) <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>=</mo> <mn>1</mn> <mo>×</mo> <msup> <mrow> <mn>10</mn> </mrow> <mrow> <mo>−</mo> <mn>7</mn> </mrow> </msup> </mrow> </semantics></math>; (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>=</mo> <mn>1</mn> <mo>×</mo> <msup> <mrow> <mn>10</mn> </mrow> <mrow> <mo>−</mo> <mn>8</mn> </mrow> </msup> </mrow> </semantics></math>.</p>
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<p>Calculated values of deviations in outer and inner radii in optimal control mode and without it, with optimal control function (in the case of the objective functional (15)): (<b>a</b>) regularization parameter (control cost) <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>=</mo> <mn>1</mn> <mo>×</mo> <msup> <mrow> <mn>10</mn> </mrow> <mrow> <mo>−</mo> <mn>7</mn> </mrow> </msup> </mrow> </semantics></math>; (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>=</mo> <mn>1</mn> <mo>×</mo> <msup> <mrow> <mn>10</mn> </mrow> <mrow> <mo>−</mo> <mn>8</mn> </mrow> </msup> </mrow> </semantics></math>.</p>
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<p>Analysis of the values of the regularization parameter <math display="inline"><semantics> <mi>α</mi> </semantics></math> (in the case of the objective functional (15)).</p>
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<p>Geometry of the drawn fiber and optimal control of the capillary drawing speed (in the case of the objective functional (16), <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>=</mo> <mn>1</mn> <mo>×</mo> <msup> <mrow> <mn>10</mn> </mrow> <mrow> <mo>−</mo> <mn>8</mn> </mrow> </msup> </mrow> </semantics></math>).</p>
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<p>Dependence of the component objective functional values (×10<sup>−5</sup>) on the regularization parameter.</p>
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12 pages, 5446 KiB  
Article
Understanding the Molecular Arrangement and Orientation Characteristics of Mesophase Pitch and Its Fibers via a Polarized Light Microscope
by Jingpan Li, Ximing Tang, Ji Qin, Jianxiao Yang, Xiao Wu, Yuxin Wei, Xubin He and Zujian Huang
Polymers 2024, 16(8), 1114; https://doi.org/10.3390/polym16081114 - 16 Apr 2024
Viewed by 1256
Abstract
A polarized light microscope (PLM) was utilized to examine the optical textures of mesophase pitch (MP) and MP-derived fibers, which aimed to reveal the arrangement and orientation characteristics of pitch molecules and to clarify the evolution and transformation mechanism of carbonaceous microcrystalline from [...] Read more.
A polarized light microscope (PLM) was utilized to examine the optical textures of mesophase pitch (MP) and MP-derived fibers, which aimed to reveal the arrangement and orientation characteristics of pitch molecules and to clarify the evolution and transformation mechanism of carbonaceous microcrystalline from pitch fibers to graphitized fibers. The results found that there were distinct optical textures in MP, where one side exhibited a transition from a flattening plane to a mountain-like undulating plane. This transition corresponded to the arrangement of pitch molecules, resembling stacked lamellar structures reminiscent of curved paper. Meanwhile, the optical textures of fibers revealed that the blue substance was wrapped around the red grain-like domains in the longitudinal section and confirmed that the red part belonged to the pyridine insoluble fraction of MP and the blue part belonged to its pyridine-soluble fraction. After graphitization, the red part was transformed into graphite sheets and the blue part was transformed into an amorphous carbon layer which was wrapped around the graphite sheets, forming a carbonaceous microcrystalline package-like bag. Therefore, this study provided a comprehensive interpretation of the structural evolution mechanism of MP and MP-derived fibers based on their macro-optical textures and micro-nanostructures. Full article
(This article belongs to the Special Issue Fiber-Reinforced Polymer Composites)
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<p>Physical sample of MP (<b>a</b>), PLM images of MP on an A-side (<b>b</b>), A’-side (<b>c</b>), B-side (<b>d</b>), C-side (<b>e</b>), enlarged view of B-C side (<b>f</b>,<b>g</b>). The arrow represents the orientation direction of the polarized structure and the green dashed line represents the intersection line of the B-C side.</p>
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<p>A relationship between polarized stripes and molecular orientation of MP proposed by Zimmer [<a href="#B14-polymers-16-01114" class="html-bibr">14</a>]. The yellow lines represent the polarization features of the corresponding molecular orientation, and the letters (a,b,c,d,e,f) represent the corresponding observation direction plane.</p>
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<p>3D PLM images’ model and molecular structure arrangement, and an orientation model of MP. The blue component of the model represents the laminar structure of MP molecule, while the orange component represents the folded structure of MP molecule.</p>
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<p>The PLM image model of MP-derived PFs based on the literature of Mochida [<a href="#B24-polymers-16-01114" class="html-bibr">24</a>]. The model is derived from the characteristic in the light blue area of PLM images (white box).</p>
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<p>PLM images of pyridine extracted MP-derived PFs (<b>a</b>,<b>b</b>) before extraction and (<b>c</b>,<b>d</b>) after extraction.</p>
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<p>The evolution model of polarizing textures of MP-derived fibers at various stages.</p>
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<p>PLM images of CFs and GFs in the cross-section between perpendicular and parallel.</p>
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<p>Raman spectra of MP-derived PFs (<b>a</b>), SFs (<b>b</b>), CFs (<b>c</b>), GFs (<b>d</b>) in the core (red part) and edge (bule part) positions of fruit-grain domain structures.</p>
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<p>The cross-section SEM images of MP-derived GFs. The top opening part (<b>a</b>–<b>c</b>), the middle part (<b>d</b>–<b>f</b>) and the bottom part (<b>g</b>–<b>i</b>) of the packages structure. The green box area shows the typical an amorphous carbon layer around the graphite sheets of GFs.</p>
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<p>The models of “package” and domain of MP-derived fibers.</p>
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16 pages, 6552 KiB  
Article
Enhancement of Flexural Strength in Fiber–Cement Composites through Modification of Sisal Fiber with Natural Rubber Latex and Expanded Perlite
by Siriwan Thepruttana, Jira Patthanavarit, Montree Hankoy, Mettaya Kitiwan, Nittaya Keawprak and Phacharaphon Tunthawiroon
Buildings 2024, 14(4), 1067; https://doi.org/10.3390/buildings14041067 - 11 Apr 2024
Viewed by 1218
Abstract
This study presents a novel approach in enhancing the flexural strength of sisal fiber cement composites by employing a dual coating technique with natural rubber latex and expanded perlite to the sisal fibers. The effects of different fiber content (0.25, 0.5, 0.75, 1, [...] Read more.
This study presents a novel approach in enhancing the flexural strength of sisal fiber cement composites by employing a dual coating technique with natural rubber latex and expanded perlite to the sisal fibers. The effects of different fiber content (0.25, 0.5, 0.75, 1, 1.25, and 1.5 wt%) and fiber length (1, 2, and 3 cm) on the physical and mechanical properties of sisal fiber cement were also studied. The physical properties, including bulk density and water absorption, were evaluated via the Archimedes method. Flexural strength was measured using the 3-point bending method, and microstructure was observed using a scanning electron microscope (SEM) and an optical microscope (OM). As the fiber content and length increase, the bulk density of the sisal fiber cement decreases. However, composites utilizing coated fibers consistently exhibit a higher bulk density than those utilizing uncoated fibers, attributed to enhanced adhesion and reduced porosity. The water absorption of sisal fiber cement increases with fiber content, but it is mitigated by the natural rubber latex coating, which prevents fiber–water absorption, and by expanded perlite, which reduces voids in the matrix. Composites containing coated fibers consistently exhibit superior flexural strength compared to those with uncoated fibers. The highest flexural strength values of 5.58 MPa were observed in composites utilizing 3 cm of coated fiber with 0.25 wt% fiber content. Microstructure analysis reveals a well-bonded interface in coated fibers, emphasizing the positive impact of coating on mechanical performance. The incorporation of coated sisal fibers effectively improves adhesion, water resistance, and flexural strength, offering sustainable and durable construction materials. The achieved results can serve as the guidelines for the development of a high-performance bio-based construction materials with improved durability and reduced environmental impact. Full article
(This article belongs to the Section Building Materials, and Repair & Renovation)
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<p>The images showing the sisal fibers characteristics: (<b>a</b>) as-received sisal fibers; (<b>b</b>) cut and cleaned sisal fibers; (<b>c</b>) alkali-treated sisal fibers or uncoated sisal fibers; and (<b>d</b>) natural rubber latex and expanded perlite-coated sisal fibers.</p>
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<p>(<b>a</b>) Schematic representation of the three-point bending setup and (<b>b</b>) testing apparatus setting in universal testing machine.</p>
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<p>SEM images showing the surface of sisal fibers: (<b>a</b>) as-received sisal fibers; (<b>b</b>) alkali-treated sisal fibers; and (<b>c</b>) natural rubber latex and expanded perlite-coated sisal fibers.</p>
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<p>Bulk density of fiber–cement composites using uncoated and coated sisal fibers, with varying fiber lengths and contents.</p>
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<p>Water absorption of fiber–cement composites using uncoated and coated sisal fibers, with varying fiber lengths and contents.</p>
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<p>Flexural strength of fiber–cement composites after 28 aging days, and a comparison between specimens using uncoated and coated sisal fibers, with varying fiber lengths and contents.</p>
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<p>Failure mode of specimens containing 0.25 wt% of 3 cm sisal fiber: (<b>a</b>) uncoated sisal fiber cement; and (<b>b</b>) coated sisal fiber cement.</p>
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<p>Optical microscope images of the surface microstructure of fiber–cement composites with (<b>a</b>) uncoated and (<b>b</b>) coated sisal fibers.</p>
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<p>SEM images of the pulled-out fibers: (<b>a</b>) uncoated; and (<b>b</b>) coated sisal fibers.</p>
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25 pages, 8377 KiB  
Review
Advancements in Battery Monitoring: Harnessing Fiber Grating Sensors for Enhanced Performance and Reliability
by Kaimin Yu, Wen Chen, Dingrong Deng, Qihui Wu and Jianzhong Hao
Sensors 2024, 24(7), 2057; https://doi.org/10.3390/s24072057 - 23 Mar 2024
Cited by 6 | Viewed by 2161
Abstract
Batteries play a crucial role as energy storage devices across various industries. However, achieving high performance often comes at the cost of safety. Continuous monitoring is essential to ensure the safety and reliability of batteries. This paper investigates the advancements in battery monitoring [...] Read more.
Batteries play a crucial role as energy storage devices across various industries. However, achieving high performance often comes at the cost of safety. Continuous monitoring is essential to ensure the safety and reliability of batteries. This paper investigates the advancements in battery monitoring technology, focusing on fiber Bragg gratings (FBGs). By examining the factors contributing to battery degradation and the principles of FBGs, this study discusses key aspects of FBG sensing, including mounting locations, monitoring targets, and their correlation with optical signals. While current FBG battery sensing can achieve high measurement accuracies for temperature (0.1 °C), strain (0.1 με), pressure (0.14 bar), and refractive index (6 × 10−5 RIU), with corresponding sensitivities of 40 pm/°C, 2.2 pm/με, −0.3 pm/bar, and −18 nm/RIU, respectively, accurately assessing battery health in real time remains a challenge. Traditional methods struggle to provide real-time and precise evaluations by analyzing the microstructure of battery materials or physical phenomena during chemical reactions. Therefore, by summarizing the current state of FBG battery sensing research, it is evident that monitoring battery material properties (e.g., refractive index and gas properties) through FBGs offers a promising solution for real-time and accurate battery health assessment. This paper also delves into the obstacles of battery monitoring, such as standardizing the FBG encapsulation process, decoupling multiple parameters, and controlling costs. Ultimately, the paper highlights the potential of FBG monitoring technology in driving advancements in battery development. Full article
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<p>Typical scheme of FBG sensors.</p>
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<p>Description of the interrogation system.</p>
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<p>Typical scheme of TFBG sensors.</p>
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<p>TFBG-based SPR optical fiber sensor [<a href="#B110-sensors-24-02057" class="html-bibr">110</a>]: (<b>a</b>) ionic concentration; (<b>b</b>) sketch of the configuration of a plasmonic fiber optic sensor; and (<b>c</b>) experimental setup for RI monitoring.</p>
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<p>Monitoring temperature changes in pouch Li-ion battery using thermocouple sensors and FBG sensors [<a href="#B13-sensors-24-02057" class="html-bibr">13</a>].</p>
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<p>FBG-based temperature measurement for cylindrical Li-ion battery: (<b>a</b>) single FBG sensing element schematic [<a href="#B115-sensors-24-02057" class="html-bibr">115</a>]; (<b>b</b>) four FBG sensing elements uniformly distributed schematic [<a href="#B116-sensors-24-02057" class="html-bibr">116</a>].</p>
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<p>Schematic of integrating FBG sensors into the central void of cylindrical jelly-roll Li-ion battery [<a href="#B117-sensors-24-02057" class="html-bibr">117</a>].</p>
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<p>Schematic diagram of FBG array thin film temperature measurement device [<a href="#B15-sensors-24-02057" class="html-bibr">15</a>].</p>
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<p>Two different approaches [<a href="#B118-sensors-24-02057" class="html-bibr">118</a>]: (<b>a</b>) internally attached FBG strain sensor on graphite anode; (<b>b</b>) internally implanted FBC strain sensor within graphite anode.</p>
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<p>FBG sensor integrated into a Li-ion coin cell [<a href="#B24-sensors-24-02057" class="html-bibr">24</a>]: (<b>a</b>) case of the coin cell; (<b>b</b>) all components of the coin cell; (<b>c</b>) SEM image of the damaged cathode at 500 micron magnification; and (<b>d</b>) SEM image of the damaged cathode at 300 micron magnification.</p>
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<p>Simultaneous monitoring of temperature and strain scheme [<a href="#B122-sensors-24-02057" class="html-bibr">122</a>]: (<b>a</b>) FBG combined with FP; (<b>b</b>) diagram of the experimental setup of a sensor network for temperature and strain monitoring of Li-ion pouch battery.</p>
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<p>Schematic diagram of the location of the FBG sensors [<a href="#B112-sensors-24-02057" class="html-bibr">112</a>].</p>
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<p>Monitor internal battery temperature and pressure: (<b>a</b>) cross-section of SMF and MOF; (<b>b</b>) SMF-FBG and MOF-FBG implanted into Li-ion battery.</p>
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<p>Schematic of typical and enhanced sensitivity optical waveguide structures [<a href="#B127-sensors-24-02057" class="html-bibr">127</a>]: (<b>a</b>) the original design, where the grating is inscribed in the fiber core; (<b>b</b>) the self-compensating design, where an additional waveguide is inscribed in the cladding to increase the refractive-index sensitivity and to direct some of the propagating light to this waveguide.</p>
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21 pages, 7838 KiB  
Review
Applications of Microstructured Optical Fibers in Ultrafast Optics: A Review
by Ziwen Tang, Zihua Zheng, Boyao Li, Zhiyi Wei and Jinghua Sun
Photonics 2024, 11(2), 151; https://doi.org/10.3390/photonics11020151 - 5 Feb 2024
Cited by 3 | Viewed by 2350
Abstract
With the development of laser technology, microstructured optical fibers (MOFs) have become an important part of ultrafast optics, providing excellent platforms for ultrafast laser pulse generation, amplification, and compression, promoting the development of fiber laser systems to generate high power, high pulse energy, [...] Read more.
With the development of laser technology, microstructured optical fibers (MOFs) have become an important part of ultrafast optics, providing excellent platforms for ultrafast laser pulse generation, amplification, and compression, promoting the development of fiber laser systems to generate high power, high pulse energy, and few-cycle duration pulses. MOFs extend the ultrafast laser spectrum to the vacuum ultraviolet (VUV) and even extreme ultraviolet (EUV) regions based on dispersive wave emission and high harmonic generation, as well as to the mid-infrared region based on soliton self-frequency shift (SSFS), contributing compact and low-cost light sources for precision microscopy and spectroscopy. In this paper, first several common types of MOFs are introduced, then the various applications of MOFs in ultrafast optics are discussed, mainly focusing on the aspects of ultrafast laser pulse scaling in pulse energy and spectral bandwidth, and finally the possible prospects of MOFs are given. Full article
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<p>Scanning electron microscope (SEM) images of the cross-section of the solid-core PCFs. (<b>a</b>) The first solid PCF [<a href="#B19-photonics-11-00151" class="html-bibr">19</a>]; (<b>b</b>) Four-core PCF [<a href="#B20-photonics-11-00151" class="html-bibr">20</a>]; (<b>c</b>) Multi-core PCF [<a href="#B21-photonics-11-00151" class="html-bibr">21</a>].</p>
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<p>SEM images of the cross section of the PBGFs. (<b>a</b>) The first honeycomb structure PBGF [<a href="#B23-photonics-11-00151" class="html-bibr">23</a>]; (<b>b</b>) All-solid PBGF (Ge-doped capillary rods inserted in the silica substrate) [<a href="#B24-photonics-11-00151" class="html-bibr">24</a>]; (<b>c</b>) The first HC-PBGF [<a href="#B25-photonics-11-00151" class="html-bibr">25</a>]; (<b>d</b>) Kagome HC-PCF [<a href="#B26-photonics-11-00151" class="html-bibr">26</a>]. (The core diameters of these PBGFs are (<b>a</b>) 0.8 μm, (<b>b</b>) 39.5 μm, (<b>c</b>) 14.8 μm, and (<b>d</b>) 170 μm).</p>
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<p>Guidance mechanisms of (<b>a</b>) Frustrated tunneling PBG effect and (<b>b</b>) Bragg PBG effect [<a href="#B25-photonics-11-00151" class="html-bibr">25</a>].</p>
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<p>SEM image of the cross-section of the ARFs. (<b>a</b>) Single ring ARF with touching point [<a href="#B28-photonics-11-00151" class="html-bibr">28</a>], (core diameter is 36 μm, the outer diameter of the single ring is 22.5 μm, inner diameter is 17.1 μm); (<b>b</b>) Conjoined-tube ARF [<a href="#B29-photonics-11-00151" class="html-bibr">29</a>], (core diameter is 30.5 μm, the yellow numbers label the five dielectric layers in the cladding); (<b>c</b>) Nested ARF [<a href="#B30-photonics-11-00151" class="html-bibr">30</a>], (core diameter is 32.5 μm, outer diameter is 25.6 μm, inner diameter is 12.1 μm).</p>
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<p>The guidance mechanism of ARF (equivalent Fabry–Perot cavity model).</p>
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<p>SEM image of the cross-section of the first Hybrid PCF [<a href="#B33-photonics-11-00151" class="html-bibr">33</a>]. The hybrid PCF is composed of air holes (black) and Ge-doped silica rods (gray rods in horizontal direction) disposed around an undoped silica core.</p>
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<p>Schematic diagram of CPA technology.</p>
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<p>(<b>a</b>) Schematic of the coherently combined fiber CPA laser system [<a href="#B41-photonics-11-00151" class="html-bibr">41</a>] (CFBG, chirped fiber Bragg gratings; FDPS, Fourier-domain pulse shaper; AOM, acousto-optic modulator; LPF, large-pitch fiber; QWP, quarter-wave plate; HWP, half-wave plate; PBS, polarizing beam splitter; TFP, thin-film polarizer); (<b>b</b>) SEM image of the cross-section of the LPF [<a href="#B44-photonics-11-00151" class="html-bibr">44</a>] (the core diameter is 135 μm).</p>
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<p>Experimental spectra of SCG. The blue curve was measured by the VUV spectrometer, and the brown curve was UV-NIR spectrometer. The solid black line is the simulated spectrum. The dashed vertical line marks the ZDW (N = normal, A = anomalous GVD) [<a href="#B60-photonics-11-00151" class="html-bibr">60</a>].</p>
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<p>Experimental setup of the compact SC source [<a href="#B67-photonics-11-00151" class="html-bibr">67</a>] (EDF: Erbium-doped fiber; GSA: graphene saturable absorber; OC: output coupler; ISO: isolator; WDM: wavelength division multiplexer; PM-HNLF: polarization maintaining highly nonlinear fiber).</p>
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<p>(<b>a</b>) SEM image of the cross section of the kagome-type HC-PCF used for HHG, where the effective mode diameter (corresponding to the hollow center core) is about 15 μm; (<b>b</b>) Measured spectrum of the HHG [<a href="#B76-photonics-11-00151" class="html-bibr">76</a>].</p>
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<p>Experimental generation of coherent ultrashort pulses through resonant dispersive wave emission in gas-filled kagome HC-PCF [<a href="#B81-photonics-11-00151" class="html-bibr">81</a>]. Each peak is the individual normalized spectrum for a specific gas, pressure, and pump energy. All the tuning was carried out in an identical length of kagomé HC-PCF (27 µm core diameter), except in the case of neon, where the core diameter was 37 µm.</p>
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<p>(<b>a</b>) Experimental setup of the two-stage ARF compressor. <span class="html-italic">λ</span>/2: half-wave plate. <span class="html-italic">λ</span>/4: quarter-wave plate. TFP: thin-film polarizer. CM: negatively chirped mirror. FM: flip mirror. OAPM: off-axis parabolic mirror. W: glass wedge. (<b>b</b>,<b>c</b>) SEM images of the ARFs, core diameters 86 µm in the first compression stage and 59 µm in the second stage [<a href="#B103-photonics-11-00151" class="html-bibr">103</a>].</p>
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<p>(<b>a</b>) Experiment setup of HHML for high repetition rate soliton generation, LD: laser diode, ISO: isolator, PC: polarization controller, SMF: single mode fiber; (<b>b</b>) <b>left</b>: SEM of the solid-core PCF, <b>right</b>: zoom-in of the core region. The two slightly smaller hollow channels marked by the red arrows render the PCF polarization-maintaining [<a href="#B112-photonics-11-00151" class="html-bibr">112</a>].</p>
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