2 Design and simulations

The structure of the dual-structure fiber grating and the principle of mitigating the SRS are shown in Figure 1. This type of grating consists of a CTFBG and an FBG structure. The spectra of the CTFBG and FBG are designed to cover the SRS completely. When the signal laser containing Stokes light transmits to the grating, the SRS will first be coupled by the CTFBG structure from the forward-transmitting core mode to the backward-transmitting cladding mode. In this case, the backward-transmitting cladding mode will contain most of the SRS power. Meanwhile, there is a small amount of signal laser in the backward-transmitting cladding mode due to the insertion loss of the CTFBG at the signal laser wavelength. Subsequently, when the signal laser continues to transmit to the FBG structure, the residual SRS light will be coupled to the backward-transmitting core mode, which is then coupled to the cladding mode again by the CTFBG. At this time, the CTFBG couples the SRS light to the forward-transmitting cladding mode. Since the FBG hardly reflects the signal laser, only the residual SRS is present in the forward-transmitting cladding mode. Finally, cladding power strippers (CPSs; CPS₁ and CPS₂) are used to strip the cladding mode from the fiber to suppress SRS. This implies that the Stokes light passes through the CTFBG twice, while the signal laser passes only once. Therefore, the dual-structure fiber grating exhibits a low insertion loss while achieving a high SRS mitigation rate.

To analyze the transmission and reflection spectra of the dual-structure fiber grating, we need to calculate the transmission and reflection spectra of the CTFBG and FBG. We first analyze the derivation of the transmission spectrum ${I}_{\mathrm{T}-\mathrm{C}}$ and reflection spectrum ${I}_{\mathrm{R}-\mathrm{C}}$ of the CTFBG. Since the CTFBG can couple the forward-transmitting core mode to the backward-transmitting core and cladding modes, the mode coupling equations of the CTFBG can be expressed as follows^[ Reference Erdogan^19, Reference Erdogan^20]:

(1a) $$\begin{align}\frac{\mathrm{d}A^{\mathrm{co re}}}{\mathrm{d}z}=\ &j\sigma \left(z,\lambda (z),\theta \right){A}^{\mathrm{co re}}+j\frac{s}{2}\sigma \left(z,\lambda (z),\theta \right){B}^{\mathrm{co re}}{e}^{-2j{\delta}^{\mathrm{co}-\mathrm{co}}z}\nonumber\\&+j\sum \limits_i\kappa \left(z,\lambda (z),\theta \right){B}_i^{\mathrm{cl ad}}{e}^{-2j{\delta}^{\mathrm{cl- co}}z},\end{align}$$

(1b) $$\begin{align}\frac{\mathrm{d}B^{\mathrm{co re}}}{\mathrm{d}z}=- j\sigma \left(z,\lambda (z),\theta \right){B}^{\mathrm{co re}}-j\frac{s}{2}\sigma \left(z,\lambda (z),\theta \right){A}^{\mathrm{co re}}{e}^{2j{\delta}^{\mathrm{co}-\mathrm{co}}z},\end{align}$$

(1c) $$\begin{align}\frac{\mathrm{d}B_i^{\mathrm{cl ad}}}{\mathrm{d}z}=-i\sum \limits_i\left({\kappa}_i(z,\lambda (z),\theta ){A}^{\mathrm{core}}{e}^{2j{\delta}^{\mathrm{cl- co}}z}\right),\end{align}$$

where ${A}^{\mathrm{core}}$ , ${B}^{\mathrm{core}}$ and ${B}_i^{\mathrm{clad}}$ , respectively, represent the complex amplitudes of the forward transmission core mode, backward transmission core mode and ith backward transmission cladding mode, $\lambda$ is the wavelength, $\theta$ is the tilted angle, $s$ represents the fringe visibility, $\sigma \left(z,\lambda (z),\theta \right)$ is the self-coupling coefficient and ${\kappa}_i\left(z,\lambda (z),\theta \right)$ represents the cross-coupling coefficient, which can be expressed as follows

(2) $$\begin{align}\sigma \left(z,\lambda (z),\theta \right)=\frac{\pi {n}_{\mathrm{core}, \mathrm{eff}}}{\lambda (z)}\overline{\Delta {n}_{\mathrm{core}}(z)}\cos \theta \underset{\mathrm{core}}{\iint}{e}\left(x,y\right){{e}}^{\ast}\left(x,y\right)\mathrm{d}x\mathrm{d}y,\end{align}$$

(3) $$\begin{align}&{\kappa}_i\left(z,\lambda (z),\theta \right)\nonumber\\&\quad=\frac{\pi {n}_{\mathrm{core}, \mathrm{eff}}}{2\lambda (z)}\overline{\Delta {n}_{\mathrm{core}}(z)}\cos \theta \underset{\mathrm{core}}{\iint }{e}^{i\frac{2\pi }{\Lambda_{\mathrm{CTFBG}}(z)}x\tan \theta}{e}\left(x,y\right){{e}}^{\ast}\left(x,y\right)\mathrm{d}x\mathrm{d}y,\end{align}$$

where ${n}_{\mathrm{core}, \mathrm{eff}}$ is the effective refractive index of the fiber core, $\overline{\Delta {n}_{\mathrm{core}}(z)}$ is the slowly variable envelope function, ${e}\left(x,y\right)$ is the transverse component of the fundamental mode electric field and ${{e}}^{\ast}\left(x,y\right)$ is its conjugation, and ${\Lambda}_{\mathrm{CTFBG}}(z)$ represents the period of the CTFBG, which can be expressed as follows:

(4) $$\begin{align}{\Lambda}_{\mathrm{CTFBG}}(z)={\Lambda}_{\mathrm{C}1}+\frac{\mathrm{Chirp}_1}{2{n}_{\mathrm{core}, \mathrm{eff}}}z/\cos \theta, \kern1.44em -\frac{L_1}{2}\le z\le \frac{L_1}{2},\end{align}$$

where ${\Lambda}_{\mathrm{C}1}$ is the center period of the CTFBG, $\mathrm{Chirp}_1$ is the chirp rate of the CTFBG and ${L}_1$ is the length of the CTFBG. Further, ${\delta}^{\mathrm{co}-\mathrm{co}}$ represents the detuning coefficient between the fiber core modes and ${\delta}^{\mathrm{cl- co}}$ represents the detuning coefficient between the cladding modes and core modes, which can be expressed as follows:

(5) $$\begin{align}{\delta}^{\mathrm{co}-\mathrm{co}}=\frac{2\pi }{\lambda }{n}_{\mathrm{co re}, \mathrm{eff}}-\frac{\pi }{\Lambda_{\mathrm{CTFBG}}},\end{align}$$

(6) $$\begin{align}{\delta}^{\mathrm{cl- co}}=\frac{\pi }{\lambda }{n}_{\mathrm{core}, \mathrm{eff}}+\frac{\pi }{\lambda }{n}_{\mathrm{cl ad}, \mathrm{eff}}^i-\frac{\pi }{\Lambda_{\mathrm{CTFBG}}},\end{align}$$

where ${n}_{\mathrm{clad}, \mathrm{eff}}^i$ is the effective index of the ith cladding mode. When Equations (5) and (6) are equal to 0, we can calculate the Bragg resonance wavelength ${\lambda}_{\mathrm{B}- \mathrm{CTFBG}}$ and cladding mode resonance wavelengths of the CTFBG, which can be expressed as follows:

(7) $$\begin{align}&{\lambda}_{\mathrm{B}- \mathrm{CTFBG}}\left(z\right)\nonumber\\&\quad=2{n}_{\mathrm{core}, \mathrm{eff}}\left({\Lambda}_{\mathrm{C}1}+\frac{\mathrm{Chirp}_1}{2{n}_{\mathrm{core}, \mathrm{eff}}}z\right)/\cos \theta, \kern1.44em -\frac{L_1}{2}\le z\le \frac{L_1}{2},\end{align}$$

(8) $$\begin{align}&{\lambda}_{\mathrm{clad},i}(z)\nonumber\\&\quad=\left({n}_{\mathrm{clad}, \mathrm{eff}}^i+{n}_{\mathrm{core}, \mathrm{eff}}\right)\!\kern-1.1pt\left({\Lambda}_{\mathrm{C}1}+\frac{\mathrm{Chirp}_1}{2{n}_{\mathrm{core}, \mathrm{eff}}}z\right)\kern-1.2pt/\cos \theta,\quad\! -\frac{L_1}{2}\le z\le \frac{L_1}{2}.\end{align}$$

Thus, ${I}_{\mathrm{T}-\mathrm{C}}$ and ${I}_{\mathrm{R}-\mathrm{C}}$ can be obtained by solving Equations (1a)–(1c), which can be expressed as follows:

(9) $$\begin{align}{I}_{\mathrm{T}-\mathrm{C}}\left(\lambda \right)=\frac{{\left|{A}_{\mathrm{core}}\left(\frac{L_1}{2}\right)\right|}^2}{{\left|{A}_{\mathrm{core}}\left(-\frac{L_1}{2}\right)\right|}^2},\quad {I}_{\mathrm{R}-\mathrm{C}}\left(\lambda \right)=\frac{{\left|{B}_{\mathrm{core}}\left(\frac{L_1}{2}\right)\right|}^2}{{\left|{A}_{\mathrm{core}}\left(-\frac{L_1}{2}\right)\right|}^2}.\end{align}$$

Compared to the CTFBG, the derivation of the transmission spectrum ${I}_{\mathrm{T}-\mathrm{F}}$ and reflection spectrum ${I}_{\mathrm{R}-\mathrm{F}}$ for the FBG is much simpler. The FBG couples the forward-transmitting fiber core modes to the backward-transmitting fiber core modes, and thus the mode coupling equation can be simplified as follows:

(10a) $$\begin{align}\frac{\mathrm{d}A^{\mathrm{co re}}}{\mathrm{d}z}= j\sigma \left(z,\lambda (z),\theta \right){A}^{\mathrm{co re}}+j\frac{s}{2}\sigma \left(z,\lambda (z),\theta \right){B}^{\mathrm{co re}}{e}^{-2j{\delta}^{\mathrm{co}-\mathrm{co}}z},\end{align}$$

(10b) $$\begin{align}\frac{\mathrm{d}B^{\mathrm{co re}}}{\mathrm{d}z}=- j\sigma \left(z,\lambda (z),\theta \right){B}^{\mathrm{co re}}-j\frac{s}{2}\sigma \left(z,\lambda (z),\theta \right){A}^{\mathrm{co re}}{e}^{2j{\delta}^{\mathrm{co}-\mathrm{co}}z}.\end{align}$$

The period of the FBG can be expressed as follows:

(11) $$\begin{align}{\Lambda}_{\mathrm{FBG}}(z)={\Lambda}_{\mathrm{C}2}+\frac{\mathrm{Chirp}_2}{2{n}_{\mathrm{core}, \mathrm{eff}}}z,\kern1.44em -\frac{L_2}{2}\le z\le \frac{L_2}{2},\end{align}$$

where ${\Lambda}_{\mathrm{C}2}$ is the center period of the FBG, $\mathrm{Chirp}_2$ is the chirp rate of the FBG and ${L}_2$ is the length of the FBG. Furthermore, the detuning coefficient ${\delta}^{\mathrm{co}-\mathrm{co}}$ can be expressed as follows:

(12) $$\begin{align}{\delta}^{\mathrm{co}-\mathrm{co}}=\frac{2\pi }{\lambda }{n}_{\mathrm{co re}, \mathrm{eff}}-\frac{\pi }{\Lambda_{\mathrm{FBG}}}.\end{align}$$

Thus, the Bragg resonance wavelength of the FBG (obtained when Equation (12) equals 0) can be expressed as follows:

(13) $$\begin{align}{\lambda}_{\mathrm{B}- \mathrm{FBG}}(z)=2{n}_{\mathrm{core}, \mathrm{eff}}\left({\Lambda}_{\mathrm{C}2}+\frac{\mathrm{Chirp}_2}{2{n}_{\mathrm{core}, \mathrm{eff}}}z\right),\kern1.44em -\frac{L_2}{2}\le z\le \frac{L_2}{2}.\end{align}$$

Further, ${I}_{\mathrm{T}-\mathrm{F}}$ and ${I}_{\mathrm{R}-\mathrm{F}}$ can also be calculated by solving Equations (10a) and (10b), which can be expressed as follows:

(14) $$\begin{align}{I}_{\mathrm{T}-\mathrm{F}}\left(\lambda \right)=\frac{{\left|{A}_{\mathrm{core}}\left(\frac{L_2}{2}\right)\right|}^2}{{\left|{A}_{\mathrm{core}}\left(-\frac{L_2}{2}\right)\right|}^2}\quad{I}_{\mathrm{R}-\mathrm{F}}\left(\lambda \right)=\frac{{\left|{B}_{\mathrm{core}}\left(\frac{L_2}{2}\right)\right|}^2}{{\left|{A}_{\mathrm{core}}\left(-\frac{L_2}{2}\right)\right|}^2}.\end{align}$$

Therefore, the transmission spectrum ${I}_{\mathrm{T}}$ of the dual-structure fiber grating, which represents the mitigation characteristics of the SRS, is determined by the transmission spectrum ${I}_{\mathrm{T}-\mathrm{C}}$ of the CTFBG and the transmission spectrum ${I}_{\mathrm{T}-\mathrm{F}}$ of the FBG. This can be calculated using Equation (15):

(15) $$\begin{align}{I}_{\mathrm{T}}\left(\lambda \right)={I}_{\mathrm{T}-\mathrm{C}}\left(\lambda \right)\times {I}_{\mathrm{T}-\mathrm{F}}\left(\lambda \right).\end{align}$$

The reflection spectrum ${I}_{\mathrm{R}}$ of the dual-structure fiber grating is determined by the backward-transmitting core mode. According to Figure 1, it can be observed that the backward-transmitting core mode consists of two parts. The first part consists of the backward-transmitting core mode ${I}_{\mathrm{R}-\mathrm{C}}$ formed by the CTFBG. The second part consists of the residual backward-transmitting core mode ${I}_{\mathrm{R}-\mathrm{C}-\mathrm{F}}$ , which is reflected by the FBG and immediately filtered by the CTFBG ( ${I}_{\mathrm{R}-\mathrm{C}-\mathrm{F}}={\left(1-{I}_{\mathrm{T}-\mathrm{C}}\right)}^2\times {I}_{\mathrm{R}-\mathrm{F}}$ ). Therefore, ${I}_{\mathrm{R}}$ can be calculated using Equation (5) as follows:

(16) $$\begin{align}{I}_{\mathrm{R}}\left(\lambda \right)=\ &{I}_{\mathrm{R}-\mathrm{C}}\left(\lambda \right)+{I}_{\mathrm{R}-\mathrm{C}-\mathrm{F}}\left(\lambda \right)\nonumber\\&+2\sqrt{I_{\mathrm{R}-\mathrm{C}}\left(\lambda \right){I}_{\mathrm{R}-\mathrm{C}-\mathrm{F}}\left(\lambda \right)}\cos \left(\frac{2\pi }{\lambda}\Delta \right),\end{align}$$

where $\Delta =\left({L}_1+{L}_2\right)/2+d$ ( $d$ is the distance between the two structures, as shown in Figure 1). In the design of a dual-structure fiber grating, we must adhere to the principle that the intensity of the backward-transmitting core mode should be low to prevent excessive Stokes light from being reflected into the laser system (this may amplify the SRS).

The intensity of the backward-transmitting core mode depends on the reflection spectrum of the dual-structure fiber grating. Thus, according to Equation (16), there are two main components that determine ${I}_{\mathrm{R}}$ , which are ${I}_{\mathrm{R}-\mathrm{C}}$ and ${I}_{\mathrm{R}-\mathrm{C}-\mathrm{F}}$ . The stronger the ${I}_{\mathrm{R}-\mathrm{C}}$ and ${I}_{\mathrm{R}-\mathrm{C}-\mathrm{F}}$ , the stronger the ${I}_{\mathrm{R}}$ . This further leads to a stronger backward transmission cladding mode.

The intensity of ${I}_{\mathrm{R}-\mathrm{C}}$ is determined by the loss rate of the CTFBG (which in turn is determined by the refractive index modulation amplitude)^[ Reference Jiao, Shu, Shen, Guan, Yang and Zhu^13]. The larger the loss rate of the CTFBG, the stronger the intensity of ${I}_{\mathrm{R}-\mathrm{C}}$ . However, the intensity of ${I}_{\mathrm{R}-\mathrm{C}}$ is usually below 20 dB^[ Reference Jiao, Shu, Shen, Guan, Yang and Zhu^13, Reference Wang, Liu, Wang, Xi and Xu^14, Reference Zhao, Tian, Wang, Li, Rao and Wang^17], and thus has a negligible effect on ${I}_{\mathrm{R}}$ . Furthermore, ${I}_{\mathrm{R}-\mathrm{C}-\mathrm{F}}$ mainly depends on two aspects. Firstly, it depends on the loss rate of the CTFBG. According to the expression of ${I}_{\mathrm{R}-\mathrm{C}-\mathrm{F}}$ , as the loss rate of the CTFBG decreases, the ${I}_{\mathrm{R}-\mathrm{C}-\mathrm{F}}$ is enhanced and subsequently causes an enhancement of the intensity of the backward-transmitting core mode. In addition, the intensity of ${I}_{\mathrm{R}-\mathrm{C}-\mathrm{F}}$ also depends on the alignment of the spectra of the CTFBG and FBG. If a mismatch between the CTFBG and FBG spectra occurs, the CTFBG will not be able to fully couple the FBG reflected backward-transmitting core mode into the cladding modes. Further, there will be a part of the residual backward-transmitting core mode that continues to be transmitted backward after passing through the CTFBG, which results in backlight enhancement.

There are two main types of mismatches. Firstly, the full-width-at-half-maximum (FWHM) of the FBG mismatches with that of the CTFBG. When the FWHM of the FBG is larger than that of the CTFBG, the CTFBG cannot fully couple the backward-transmitting core mode, reflected by the FBG, to the cladding. This further results in the enhancement of the backward light. Secondly, the center wavelength of the FBG mismatches with that of the CTFBG. This also means that the CTFBG cannot fully couple the backward transmitting to the cladding. Therefore, we need to explore the effect of the loss rate of the CTFBG, the FWHM of the FBG and the center wavelength of the FBG on the dual-structure fiber grating’s spectra.

Figure 2

Influence of the CTFBG’s loss rate on the dual-structure fiber grating. (a) Transmission and (b) reflection spectra of the CTFBG with different refractive index modulation amplitudes. The tilt angle of the CTFBG is 6°, the period is 395.5 nm, the chirp rate is 1 nm/cm and the length is 40 mm. (c) Transmission and (d) reflection spectra of the FBG. The period of the FBG is 390.5 nm, the chirp rate is 1 nm/cm, the length is 40 mm and the refractive index modulation amplitude is 0.0007. Calculated (e) transmission and (f) reflection spectra of the dual-structure fiber grating.

Figure 3

Influence of the FBG’s FWHM on the dual-structure fiber grating. (a) Transmission and (b) reflection spectra of the CTFBG with the refractive index modulation amplitude of 0.007 (the other parameters are the same as those in Figure 2). (c) Transmission and (d) reflection spectra of the FBG at different lengths. The period of the FBG is 390.5 nm, the chirp rate is 1 nm/cm and the refractive index modulation amplitude is 0.0007. Calculated (e) transmission and (f) reflection spectra of the dual-structure fiber grating.

The effect of the loss rate of the CTFBG on the spectra of the dual-structure fiber grating is explored first. The simulation results are shown in Figure 2. We set the tilt angle  $\theta$ of the CTFBG to 6°, period ${\Lambda}_{\mathrm{C}1}$ (center position) to 395.5 nm, length ${L}_1$ to 40 mm and chirp rate to 1 nm/cm. To obtain the transmission and reflection spectra of the CTFBGs with different loss rates, we set the refractive index modulation amplitude ${n}_1$ of the CTFBGs to 0.002, 0.005, 0.007 and 0.010, respectively, as shown in Figures 2(a) and 2(b). The center wavelength of the cladding mode resonance of the CTFBG is 1135 nm and the FWHM is approximately 13 nm, which can span the SRS spectrum. Regarding the FBG, the period ${\Lambda}_{\mathrm{C}2}$ is set to 390.5 nm, length ${L}_2$ to 40 mm, index modulation amplitude to 0.0007 and chirp rate to 1 nm/cm. The designed spectra are presented in Figures 2(c) and 2(d). The calculation results show that the center wavelength of the FBG matches that of the CTFBG, and its FWHM (11.0 nm) is slightly smaller than that of the CTFBG. In addition, the reflectivity of the FBG is set to more than 20 dB to ensure a high SRS mitigation ratio for the dual-structure fiber grating. Furthermore, to reduce the length of the dual-structure fiber grating, we placed an FBG 5 mm after the CTFBG, as shown in Figure 1. According to Equations (1) and (2), the spectra of the dual-structure fiber grating are calculated, as shown in Figures 2(e) and 2(f). The simulation results show that the loss rate of the CTFBG significantly influences the reflection spectrum of the grating. As the loss rate decreases, the reflection spectrum intensity of the dual-structure fiber grating gradually increases, which enhances the Stokes light energy transmitted in the reverse direction in the fiber laser system, causing an SRS surge. Therefore, we hope that the loss rate of the CTFBG will be as high as possible. However, in practice, it is difficult to achieve a high loss rate by improving the photosensitivity of the fiber and energy of the inscribing UV laser. In addition, the high loss rate increases the insertion loss of the CTFBG. Thus, we control the loss rate of the CTFBG at 20 dB. In this case, the reflection intensity of the dual-structure fiber grating is lower than –20 dB and the loss rate of the grating reaches 40 dB.

Subsequently, the influence of the FWHM of the FBG on the dual-structure fiber grating is investigated. The results are shown in Figure 3. The refractive index modulation amplitude of the CTFBG is 0.007 (corresponding to a loss rate of 20 dB) and the other parameters are the same as before. The corresponding spectra are shown in Figures 3(a) and 3(b). The FWHM of the FBG is varied by controlling its length, which is set to 20, 30, 40 and 50 mm, corresponding to the FWHM values of 6, 9, 11 and 14 nm, respectively. The other parameters remain unchanged, and the transmission and reflection spectra are shown in Figures 3(c) and 3(d). The calculated spectra of the dual-structure fiber grating are shown in Figures 3(e) and 3(f). The simulation results show that when the FWHM of the FBG is smaller than that of the CTFBG, it primarily affects the bandwidth of the dual-structure fiber grating at the highest loss rate. As the FWHM of the FBG decreases, the bandwidth at the highest loss rate of the dual-structure grating also decreases. When the FWHM of the FBG is larger than that of the CTFBG, spikes occur in the reflection spectrum of the dual-structure fiber grating. However, this violates the design principles. Therefore, the FBG length is set to 40 mm (corresponding to a bandwidth of 11.0 nm). At this point, the bandwidth at the highest loss rate of the dual-structure fiber grating could cover the SRS, and the intensity of the reflection spectrum could be controlled to values below –20 dB.

Finally, we change the center wavelength of the FBG by controlling its period to investigate the effect of the match between the center wavelengths of the CTFBG and FBG on the dual-structure fiber grating. The parameters of the CTFBG are the same as before, and the spectral data are shown in Figures 4(a) and 4(b). The period of the FBG is set to 389.9, 390.2, 390.5 and 390.9 nm, which corresponds to the center wavelengths of 1133, 1134, 1135 and 1136 nm, respectively. The other FBG parameters are the same as before, and the simulation spectra are shown in Figures 4(c) and 4(d). Therefore, we can calculate the transmission and reflection spectra of the dual-structure fiber grating, as shown in Figures 4(e) and 4(f). Large spikes appear in the reflection spectra when the center wavelength of the FBG mismatches that of the CTFBG. Unfortunately, this violates the design principles.

Figure 4

Influence of the FBG’s center wavelength on the dual-structure fiber grating. (a) Transmission and (b) reflection spectra of the CTFBG (the parameters are the same as those in Figure 3). (c) Transmission and (d) reflection spectra of the FBG at different periods. The length of the FBG is 40 nm, the chirp rate is 1 nm/cm and the refractive index modulation amplitude is 0.0007. Calculated (e) transmission and (f) reflection specta of the dual-structure fiber grating.

In conclusion, we summarize the design concepts of dual-structure fiber gratings. Firstly, the loss rate of the CTFBG is maintained at approximately 20 dB. Secondly, the FWHM of the FBG should cover the SRS range as much as possible but can be slightly smaller than that of the CTFBG. Finally, the center wavelength of the FBG must match that of the CTFBG. Therefore, we choose the following design parameters of the CTFBG in the dual-structure fiber grating: tilt angle 6°, period 395.5 nm, chirp rate 1 nm/cm, length 40 mm and loss rate 20 dB. Further, the design parameters of the FBG are period 390.5 nm, chirp rate 1 nm/cm, length 40 mm, reflectivity more than 20 dB and distance from the CTFBG 5 mm. The simulated spectra of the dual-structure fiber grating are shown in Figures 5(a) and 5(b). The center wavelength of the fiber grating is 1135 nm, the FWHM is approximately 13.1 nm and the loss rate is more than 40 dB.

Figure 5

Design results of the dual-structure fiber grating’s (a) transmission and (b) reflection spectra. The center wavelength of the designed fiber grating is 1135 nm, the FWHM is approximately 13.1 nm and the loss rate is more than 40 dB.

Figure 6

Schematic of the inscription process of the dual-structure fiber grating.

3 Fabrication

A phase mask based scanning method^[ Reference Jiao, Shu, Shen, Guan, Yang and Zhu^13] is used to inscribe the dual-structure fiber grating and an argon-ion laser (Innova 90C FreD Ion Laser, Coherent, Inc.) is utilized as the lithography laser source. According to the design parameters obtained in Section 2, phase mask 1 for the CTFBG has a period ${\Lambda}_{\mathrm{P}1}$ of 791 nm, a chirp rate ${\mathrm{Chirp}}_{\mathrm{P}1}$ of 2 nm/cm and a length ${L}_1$ of 40 mm, whereas phase mask 2 for the FBG has a period ${\Lambda}_{\mathrm{P}2}$ of 781 nm, a chirp rate ${\mathrm{Chirp}}_{\mathrm{P}2}$ of 2 nm/cm and a length ${L}_2$ of 40 mm. The inscription process is divided into four steps, as shown in Figure 6. Firstly, the hydrogenated fiber (18 days at 13 MPa and 40°C, Nufern LMA-GDF-25/400-HP-M) is aligned with phase mask 1. Subsequently, phase mask 1 is rotated so that there is an angle ${\theta}_{\mathrm{R}}$ between it and the fiber axial direction. As the fiber is equivalent to a cylindrical lens, the interference field incident on the fiber core will be distorted^[ Reference Jiao, Shu, Shen, Guan, Yang and Zhu^13], thus resulting in an error between the tilt angle $\theta$ of the CTFBG and the rotation angle ${\theta}_{\mathrm{R}}$ .The relationship between these parameters can be expressed by using Equation (17):

(17) $$\begin{align}\theta =\frac{\pi }{2}\hbox{-} \arctan {\left({n}_{\mathrm{UV}}\tan {\theta}_{\mathrm{R}}\right)}^{-1},\end{align}$$

where ${n}_{\mathrm{UV}}$ is the refractive index of the fiber core at 244 nm. Thus, to realize the inscription of the CTFBG with tilt angle of 6°, the template is rotated to approximately 4.2° relative to the fiber. The power of the UV laser is set to 100 mW, and the inscription speed is set to 0.0015 mm/s. This is because the refractive index modulation amplitude of the CTFBG is large (0.007, which means that the CTFBG is difficult to inscribe), so a high inscription power with low scanning speed is required to inscribe the CTFBG with a high loss rate. When the UV laser power is set to 100 mW (the highest power), it is found by testing different scanning speeds that the loss rate of the inscribed CTFBG could reach more than or equal to 20 dB only when the scanning speed is less than or equal to 0.0015 mm/s. Secondly, after inscribing the CTFBG, the template is rotated parallel to the fiber. Thirdly, the height of the template is increased so that phase mask 2 can be aligned with the fiber. Finally, the fiber is translated 5 mm to the left, and the FBG inscription is initiated. The inscription speed is set to 0.006 mm/s, because the refractive index modulation amplitude for the FBG is small (0.0007, which means the FBG is relatively easy to inscribe), and therefore the scanning speed could increase while the power remains unchanged. When the scanning speed is less than or equal to 0.006 mm/s, the reflectivity of the inscribed FBG can reach more than or equal to 20 dB. However, these parameters are not unique; if the UV power is reduced, then the scanning speed needs to be further reduced. If a UV laser with higher output power is applied, the scanning speed can be appropriately increased.

Furthermore, to improve the power durability of the dual-structure fiber grating, our proposed dual-annealing process, which combines constant-low-temperature and dynamic-high-temperature^[ Reference Jiao, Shu, Shen, Guan, Yang and Zhu^13, Reference Bian, Jiao, Wu, Shen, Yang and Zhu^21, Reference Jiao, Shen, Yang, Wu, Bian and Zhu^22], is adopted. The grating is first subjected to a temperature of 60°C for 30 days to remove residual dissociative hydrogen molecules. Then the grating is slowly heated to 350°C at intervals of 50°C from 23°C, and maintained at 350°C for 20 min before being gradually cooled to 23°C to decrease the concentration of hydroxyl compounds. The thermal slope of the grating before annealing is approximately 0.5°C/W, yet it is reduced to 0.016°C/W after the heating process, which allows our grating to handle a multi-kW power laser. In addition, optimizing the annealing process or utilizing femtosecond laser inscribing technology will make the dual-structure fiber grating handle a higher laser power. Figures 7(a) and 7(b) show the transmission and reflection spectra of the fabricated dual-structure fiber grating, respectively. The center wavelength is 1134.91 nm and the FWHM is approximately 13.9 nm. However, due to the low power of the ASE source for the measurement, the transmission spectral curve of the fabricated grating could not be fully measured, resulting in an observable loss rate of more than or equal to 35 dB (99.97%). Moreover, it can be observed that no peaks appear in the reflection spectrum, which means that the dual-structure fiber grating hardly reflects the SRS light back into the laser system.

Figure 7

(a) Transmission and (b) reflection spectra of the fabricated dual-structure fiber grating. The center wavelength of the grating is 1134.91 nm, the FWHM is approximately 13.9 nm and the loss rate is more than or equal to 35 dB (99.97%).

Figure 8

High-power fiber MOPA system for evaluating the dual-structure fiber grating’s performance of mitigating SRS.

Figure 9

Output spectra of the evaluation system (a) without a fiber grating, (b) with one single CTFBG, (c) with a dual-structure fiber grating and (d) comparison of these three cases when the pump power of the amplifier reaches 4800 W.

4 Experiments and results

A high-power fiber MOPA laser is established to evaluate the performance of the dual-structure fiber grating in mitigating SRS, as shown in Figure 8. The seed consists of two 976 nm laser diodes (LDs) with an output power of 200 W, a 2 × 1 combiner, a resonant cavity and a CPS (CPS-1, for stripping the residual pump light, while preventing the seed from being damaged by the reverse pump light generated by the amplifier). The resonant cavity is composed of a 7 m ytterbium-doped active fiber (LMA-YDF-20/400-M, Nufern Corporation) and a pair of 1080 nm FBGs. The reflectivity of the high-reflection (HR)-FBG is 99.6% and that of the output-coupling (OC)-FBG is 11%. The FWHMs of the HR-FBG and OC-FBG are approximately 3 and 1 nm, respectively. The reason why we chose a 7 m ytterbium-doped fiber is mainly to shorten the fiber length of the oscillator fiber, thus increasing the SRS excitation threshold and avoiding the generated SRS light being amplified by the amplifier^[ Reference Zheng, Han, Li, Li, Wang and Zhu^23]. The final output power of the seed is 250 W. Further, the amplifier adopts a bi-directional pumping structure. The forward pumping module consists of a (6 + 1) × 1 combiner and four 976 nm LDs with an output power of 400 W. The reverse pumping module consists of an (8 + 1) × 1 combiner and eight 976 nm LDs with an output power of 400 W. The ratio of the forward and reverse pump power is 1:2 in order to suppress the transverse mode instability (TMI)^[ Reference Li, Han, Chen, Li, Wang, Zheng, Yan and Zhu^24– Reference Tao, Ma, Wang, Zhou and Liu^26]. A 15 m ytterbium-doped active fiber (LMA-YDF-25/400-M, Nufern Corporation) is utilized as the gain fiber. The amplified signal laser is output through the CPSs (CPS-2 and CPS-3) and through a quartz block of high power (QBH). The dual-structure fiber grating is spliced between CPS-2 and CPS-3. CPS-2 is used to strip the residual pump power, as well as the backward-transmitting cladding modes generated by the dual-structure fiber grating (containing a small fraction of the signal laser and most of the SRS light). Furthermore, CPS-3 is used to strip the forward-transmitting cladding modes (mainly including residual SRS light) produced by the dual-structure fiber grating. The output spectra of the evaluation system are measured by detecting the scattered light from the power meter using an optical spectrum analyzer (OSA). Therefore, the SRS mitigation ratio of the fiber grating can be evaluated by comparing the output spectra before and after the grating is inserted into the amplifier of the MOPA system.

Figure 9(a) shows the output spectra of the evaluation system. When the output power exceeds 3 kW, significant SRS occurs. The center wavelength of the Stokes light is approximately 1135 and 55 nm away from the signal light. When the system output power reaches 3392 W (amplifier pump power of 4800 W), a 22.6 dB intensity difference exists between the SRS light and the signal light. Furthermore, we splice a single CTFBG between CPS-2 and CPS-3. The FWHM of the CTFBG is approximately 12.8 nm and the extinction of SRS is 18 dB (98.4%). The output spectra are shown in Figure 9(b). It can be clearly observed that the CTFBG exhibits significant attenuation of SRS light. When the output power is lower than 3 kW, the SRS light is almost invisible. However, when the power further increase to 3256 W (amplifier pump power of 4800 W), a slight SRS appears in the spectrum. The SRS peak differs from that of the signal light by 39.1 dB. This is because the mitigation capacity of the single CTFBG reaches its limit. Furthermore, the slight decrease in the signal intensity is attributed to the insertion loss of the CTFBG. A comparison of the blue spectral curves in Figures 9(a) and 9(b) shows that the system does not excite SRS in either state. Therefore, the insertion loss of the CTFBG can be calculated as (2656 W – 2573 W)/2656 W × 100% = 3.1%. The dual-structure fiber grating is then spliced into the system and the output spectra are shown in Figure 9(c). The SRS light disappears when the output power reaches 3247 W (amplifier pump power of 4800 W). Moreover, the SRS mitigation ratio of the dual-structure fiber grating exceeds 30 dB (99.9%). It is worth mentioning that the insertion loss of the fiber grating exhibits almost no increase compared with that of a single CTFBG, whereas the SRS mitigation ratio increases. This demonstrates the advantage of the dual-structure fiber grating. Figure 9(d) shows the output spectra of the MOPA system without a fiber grating, with a single CTFBG and with a dual-structure fiber grating, respectively, when the pump power of the amplifier reaches 4800 W. The insertion loss of the dual-structure fiber grating can also be calculated by comparing the blue spectral curves in Figures 9(a) and 9(c) as (2656 W – 2570 W)/2656 W × 100% = 3.2%. In addition, TMI is the main reason to limit the further increase of the output power of the system. This is mainly due to unwanted heat generating in the fiber laser system^[ Reference Smith and Smith^27– Reference Distler, Möller, Strecker, Vega, Walbaum and Schreiber^31]. Firstly, the low efficiency of the amplifier causes part of the pump power to be converted into heat. Secondly, the high-order modes (HOMs) are excited and partially leak at the fiber bend, which in turn causes the fiber to heat up. Thirdly, the thermal management of the test system is not optimized, resulting in a low heat conduction rate of the fiber, which ultimately causes heat due to heat accumulation. Aiming at this issue, we will apply tandem pumping technology and optimize the structure of the system to increase the excitation threshold of TMI in the future, and thus enhance the output power and slope efficiency of the fiber laser.

Figure 10

Output power versus amplifier pump power of the three cases. The slope efficiencies of the system for the three cases are 68.8%, 65.1% and 65.2%, respectively. In addition, the M ² values of the MOPA system for the three conditions (amplifier pump power of 4800 W) are 2.36, 2.41 and 2.42, respectively.

Figure 10 shows the slope efficiencies of the system for the three cases, which are 68.8%, 65.1% and 65.2%, respectively. Figure 10(a) shows the evolution of the beam quality when the fiber grating is not inserted. It can be seen that the beam quality is deteriorating as the power increases. This may be caused by two reasons, the first of which is the excitation of the HOMs^[ Reference Li, Han, Chen, Li, Wang, Zheng, Yan and Zhu^24] and the second is the excitation of the SRS effect, which may slightly cause mode distortion^[ Reference Chu, Shu, Chen, Li, Yan, Guo, Lin, Wang, Jing, Tang and Tao^3]. When the amplifier pump power reaches 4800 W, M ² reaches 2.35. Further, the beam qualities of the MOPA system with a single CTFBG and a dual-structure fiber grating are measured and analyzed, respectively, as shown in Figures 10(b) and 10(c). When the amplifier pump power reaches 4800 W, M ² with a single CTFBG is 2.41 and M ² with a dual-structure fiber grating is 2.42. It can be clearly observed that the beam quality of the system shows a slight degradation after splicing the fiber gratings, which is caused by the distributed non-rotation symmetry of the refractive index modulation of the CTFBG structure^[ Reference Song, Yan, Wu, Shen, Feng, Liu, Li, Chu, Li, Wang and Tao^18]. However, the beam quality of the system does not change significantly in either case of splicing the CTFBG or the dual-structure fiber grating. This is because the refractive index modulation distribution of the FBG structure is approximately rotationally symmetric. Furthermore, the refractive index modulation amplitude of the FBG is also smaller than that of the CTFBG, which has almost no effect on the beam quality. This is another advantage of the dual-structure fiber grating.

Figure 11

(a) Transmission and (b) reflection spectra of the mismatched dual-structure fiber grating. (c) Output spectra of the evaluation system with the mismatched dual-structure fiber grating.

We further test the influence on SRS mitigation when the center wavelength of the CTFBG mismatches that of the FBG. Figures 11(a) and 11(b) show the transmission and reflection spectra of the dual-structure fiber grating when a mismatch occurs. Due to the mismatch in the center wavelength, the reflection spectrum of the fiber grating yields a peak at 1137 nm. Figure 11(c) shows the output spectra after connecting the fiber grating to the MOPA system. When the laser power is below 3 kW, the mismatched dual-structure fiber grating exhibits a good mitigation ratio. However, when the laser power is further increased to 3244 W (amplifier pump power of 4800 W), the system excites the SRS light at 1137 nm again. This is due to the mismatched fiber grating coupling of non-negligible SRS light into the backward-transmission core mode, which in turn causes the backward SRS light to be amplified by the laser system. This phenomenon is similar to that observed when using CTFBGs with a small tilt angle to suppress SRS (CTFBGs with small tilt angles also couple non-negligible SRS into the backward-transmission core mode)^[ Reference Tian, Zhao, Wang, Hu, Li, Rao, Xiao and Wang^16, Reference Liu, Guo, Wu, Guan, Lu, Tam and Albert^32]. The experimental results demonstrate the necessity for the alignment of the CTFBG and FBG in the dual-structure fiber grating.

In addition, to demonstrate that the insertion loss of the CTFBG is enhanced with the increase of loss rate, we further fabricate three 6° CTFBGs with loss rates of approximately 30 dB and measure their insertion loss. The loss rates of CTFBG-1, CTFBG-2 and CTFBG-3 are 32, 29.5 and 30 dB, respectively. The transmission spectra of the three CTFBGs are shown in Figure 12. According to the previous experiments, when the output power of the fiber MOPA laser system is less than or equal to 2656 W, there is no SRS effect in the output laser spectrum. Therefore, at this power, if the output power of the system decreases after inserting the CTFBGs, it is only caused by the insertion loss of the CTFBGs. Then the insertion loss of each of the three CTFBGs can be calculated. Table 1 shows the output powers and insertion losses of the system before and after inserting the three CTFBGs. The insertion loss of CTFBG-1 is 6.70%, that of CTFBG-2 is 6.10% and that of CTFBG-3 is 6.33%. The experimental results indicate that the insertion loss of the CTFBG is proportional to the loss rate. A higher loss rate brings a higher insertion loss. When the loss rate of the CTFBG reaches 30 dB, its insertion loss will be more than 6%. This further demonstrates that enhanced refractive index modulation amplitude leads to increased CTFBG insertion loss (Figure 12).

Table 1

Insertion loss with no CTFBG, with CTFBG-1, with CTFBG-2 and with CTFBG-3.

Figure 12

Transmission spectra of (a) CTFBG-1, (b) CTFBG-2 and (c) CTFBG-3. The loss rates are 32, 29.5 and 30 dB, respectively.