Photonic Generation of Frequency 16-Tupling Millimeter-Wave Signal without Optical Filter

Xuan Li¹, Shanghong Zhao¹, Guodong Wang¹, Jingshang Liu²

¹Information and Navigation College, Air Force Engineering University, Xi’an, China.
²Troops with No. 93147, Chongqing, China.

DOI: 10.4236/jamp.2021.911193                

Abstract

A generalized optical filterless approach to achieve photonic generation of frequency 16-tupling millimeter-wave (mm-wave) signal based on two cascaded dual-parallel Mach-Zehnder modulators (DPMZMs) is presented. A theoretical analysis leading to the operating conditions to achieve frequency 16-tupling is developed. Different modulation indices (MIs) can be implemented to achieve the frequency multiplication by adjusting the delay of tunable optical delay line (TODL). It is confirmed by simulation that the proposed scheme is effective, and the radio frequency spurious suppression ratio (RFSSR) of the generated frequency 16-tupling signal can be as high as 40 dB when the sub-MZMs have extinction ratios of 30 dB. Influencing factors such as extinction ratio, DC bias drift, phase shift deviation and RF voltage deviation on the performance of optical sideband suppression ratio (OSSR) and RFSSR are also investigated.

Keywords

Millimeter-Wave Signal, Frequency 16-Tupling, Dual-Parallel Mach-Zehnder Modulator

1. Introduction

Microwave generation by photonic techniques has been intensively investigated for the advantages of low phase noise, high frequency and wide frequency tunability [1] [2]. Many approaches for photonic generation of microwave have been demonstrated in the few past years. Among them, external modulation based on Mach-Zehnder modulator (MZM) for optical frequency multiplication has been considered as an attractive solution due to the system simplicity, operation stability, large frequency tunability and high spectral purity of the generated microwave signal [1] [2] [3].

For the external modulation approaches, frequency quadrupling [2]-[8], sextupling [1] [9] and octupling [1] [10] [11] [12] signals have been achieved. To generate higher frequency signal or further reduce the need for the response bandwidth of the modulator, a higher multiplication factor is needed. A frequency 12-tupling scheme was proposed by using a DPMZM, a semiconductor optical amplifier and an optical inter-leaver (IL) [13], the OSSR was 30 dB for the generated optical signal after the IL, however, the system was complicated, and the IL worked as an OF which limited the utilization for wavelength-division-multiplexing (WDM) systems. A frequency 16-tupling signal can be generated by using two parallel DPMZMs with RFSSR as high as 55 dB [12], but the MI as 5.520 or 8.654 was too high to realize for a commercial DPMZM. An optical filterless scheme based on three parallel MZMs was proposed to achieve multiplication factors as high as 12 and 18 with RFSSRs as 50 dB and 32 dB respectively [14], however, the scheme was hard to practically utilize for the same reason that the MIs should be 5.520 and 9.761 respectively. The two cascaded DPMZMs scheme can be used to generate a frequency 16-tupling signal [15], but no generalized investigation has been reported.

In this paper, a generalized approach to generate 16-tupling mm-wave signal using two cascaded DPMZMs is presented. The significance of the configuration is that different MIs can be implemented to achieve the frequency 16-tupling while the MIs are smaller than 4, which is more practical for utilization. In addition, since no OF is required, the proposal can be used in WDM systems. Optical mm-wave signals with frequencies up to 640 GHz can be achieved by the proposed scheme if two commercially available 40 GHz DPMZMs and a wide enough bandwidth PD are employed.

2. Principle

The proposed scheme using two cascaded DPMZMs to achieve frequency 16-tupling mm-wave signal is shown in Figure 1. The system consists of a laser diode (LD), two DPMZMs, a tunable optical delay line (TODL), a photodiode (PD), a local oscillator (LO), an electrical phase shifter (PS), and three electrical power dividers. A low-frequency microwave signal from the LO is divided into

Figure 1. Two cascaded DPMZMs scheme for 16-tupling mm-wave generation. LD, laser diode; LO, local oscillator; PS, phase shifter; TODL, tunable optical delay line; PD, photodiode.

four paths by three power dividers, and applied to the two DPMZMs. The PS is used after the first power divider to introduce a phase difference between two sub-MZMs of each of the DPMZMs. The TODL can be replaced by two electrical PSs [15]. The function of TODL is to introduce a phase difference between different optical sidebands. Erbium-doped fiber amplifier (EDFA) may be used to boost the optical power of the signals output from DPMZMs.

Assuming that the incident light wave is E₀cos(ω_ct), where E₀ is the amplitude of the optical field, and ω_c is the angular frequency of incident light wave. Both the sub-MZMs of DPMZM1 are biased at the maximum transmission point (MATP) to suppress the odd-order sidebands, and the main MZM of DPMZM1 is set to let the signals from the two arms in phase. The phase difference introduced by PS is π/2, and then the optical field at the output of the DPMZM1 can be expressed as

$E_1\left(t\right)\approx E_{\text{0}}{J}_0\left(m\right)\cos {\omega }_{c}t+E_{\text{0}}{J}_4\left(m\right)\left[\cos \left({\omega }_{c}t-4\omega t\right)+\cos \left({\omega }_{c}t+4\omega t\right)\right]$ (1)

where ω is the angular frequency of the electrical driving signal, m is the MI of DPMZM1, J_n is the nth-order Bessel function of the first kind. As can be seen, only the carrier and ±4th-order sidebands are obtained. When the light wave is traveling through the TODL, a phase difference φ between the two adjacent sidebands would be introduced and the optical field E_TOD(t) at the output of the TODL can be written as [1]

$\begin{array}{l}{E}_{TOD}\left(t\right)=E_{\text{0}}{J}_0\left(m\right)\cos \left({\omega }_{c}t+2\phi \right)\\ +E_{\text{0}}{J}_4\left(m\right)\left[\cos \left({\omega }_{c}t-4\omega t+\phi \right)+\cos \left({\omega }_{c}t+4\omega t+3\phi \right)\right]\end{array}$ (2)

E_TOD(t) is then sent into DPMZM2. The DPMZM2 is biased identical to the case of DPMZM1, and the MI of DPMZM2 is also m. The optical field at the output of DPMZM2 can be expressed as

$\begin{array}{c}{E}_2\left(t\right)=E_0\{J_0^2\left(m\right)\cos \left({\omega }_{c}t+2\phi \right)+J_0\left(m\right)J_4\left(m\right)[\cos \left({\omega }_{c}t-4\omega t+2\phi \right)\\ +\cos \left({\omega }_{c}t+4\omega t+2\phi \right)]+J_0\left(m\right)J_4\left(m\right)\cos \left({\omega }_{c}t-4\omega t+\phi \right)\\ +J_4^2\left(m\right)\left[\cos \left({\omega }_{c}t-8\omega t+2\phi \right)+\cos \left({\omega }_{c}t+\phi \right)\right]\\ +J_0\left(m\right)J_4\left(m\right)\cos \left({\omega }_{c}t+4\omega t+3\phi \right)\\ +J_4^2\left(m\right)\left[\cos \left({\omega }_{c}t+3\phi \right)+\cos \left({\omega }_{c}t+8\omega t+3\phi \right)\right]\}\end{array}$ (3)

If the following conditions are satisfied

$\{\begin{array}{l}\phi =\left(2k+1\right)\pi /2\\ J_0\left(m\right)=0\end{array}$ or $\{\begin{array}{l}\phi =\left(2k+1\right)\pi \\ J_0^2\left(m\right)=2J_4^2\left(m\right)\end{array}$ (4)

where k is an integer, E₂(t) can be simplified into

$E_2\left(t\right)=E_0\left\{J_4^2\left(m\right)\left[\cos \left({\omega }_{c}t-8\omega t+2\phi \right)+\cos \left({\omega }_{c}t+8\omega t+3\phi \right)\right]\right\}$ (5)

As can be seen, only the ±8th-order sidebands are presented, the beating of the two sidebands at the PD would generate a frequency 16-tupling mm-wave signal.

Figure 2 schematically depicts the principle of the proposed mm-wave generation scheme. Optical spectra with order of 4n sidebands are performed for both of DPMZM1 and DPMZM2. There are two methods to achieve a frequency 16-tupling signal with the proposed scheme. For the first method, as shown in the upper part of Figure 2, the MI is set to make the carrier be suppressed, and only ±4th-order sidebands are presented at the output of DPMZM1. An additional phase delay π between the two components is introduced by TODL. At the output of DPMZM2, the ±4th-order sidebands are suppressed as the MI is set to make the value of J₀(m) equals to 0, and the two optical components with the same frequency as the original incident light wave are also suppressed as they have identical amplitudes and opposite phases. For the other method, as shown in the lower part of Figure 2, the carrier is not suppressed at the output DPMZM1 and three components are presented. A phase difference π between the carrier and ±4th-order sidebands is introduced by the TODL. At the output of DPMZM2, the two +4th-order sidebands, two −4th-order sidebands and the three carrier sidebands are vanished respectively, for they have identical amplitudes and opposite phase. Thus, only the ±8th-order sidebands are presented at the output of the system.

3. Simulation Results and Discussion

A concept-proof of frequency 16-tupling optical mm-wave generation is built based on the OptiSystem to verify the proposed scheme. The laser frequency is 193.1 THz with an output power of 10 dBm, the LO frequency is 10 GHz, the insert loss of DPMZM is 5 dB, the extinction ratios of sub-MZMs are 30 dB, the responsivity of PD is 0.65 A/W.

Firstly, the conditions presented in equation (4) are calculated. When 0 < m < 5, the value of J₀(m) will be equal to 0 when m = 2.405, and the condition J₀²(m) = 2J₄²(m) will be satisfied when m = 2.265, 2.672 or 3.999. Therefore, there are four MIs can be used for the proposed approach to generate a 16-tupling mm-wave signal.

The MI is set as 2.405 to suppress the carrier, and the time delay of the TODL is set as 11/160 ns, an EDFA with gain of 15 dB and noise figure of 4 dB is placed

Figure 2. Illustration for the proposed mm-wave generation.

after DPMZM1, and another EDFA with gain of 25 dB and noise figure of 4 dB is placed after DPMZM2, the average receiving optical signal power of PD appropriates −4 dBm. Simulation results are given in Figure 3. The dashed line in Figure 3(a) represent the power spectral density of amplifier spontaneous emission (ASE) noise induced by EDFAs. It can be seen that a 160 GHz mm-wave signal is generated by a 10 GHz oscillator. Several optical sidebands are presented and the fifth-order sidebands become the second dominant components. In the electrical domain, the RFSSR is limited by the tenth-order harmonic component. The measured OSSR and RFSSR of the generated mm-wave signal are degraded to 9 dB and 18 dB respectively, as shown in Figure 3(a) and Figure 3(b).

The MI is set as 2.265, the time delay of the TODL is set as 11/80 ns, an EDFA with gain of 15 dB and noise figure of 4 dB is placed after DPMZM1, and another EDFA with gain of 29 dB and noise figure of 4 dB is placed after DPMZM2, the average receiving optical signal power of PD appropriates −4 dBm. Simulation results are given in Figure 4. For the generated optical signal, many components are presented and the OSSR is only 4 dB. In the electrical domain, the even-order harmonic components are appeared and the RFSSR only

(a) (b)

Figure 3. (a) Optical, (b) electrical spectrum when m = 2.405.

(a) (b)

Figure 4. (a) Optical, (b) electrical spectrum when m = 2.265.

appropriates 1 dB. To obtain the generated 160 GHz mm-wave signal, an electrical filter is needed.

The MI is set as 2.672, the time delay of the TODL is set as 11/80 ns, an EDFA with gain of 15 dB and noise figure of 4 dB is placed after DPMZM1, and another EDFA with gain of 19 dB and noise figure of 4 dB is placed after DPMZM2, the average receiving optical signal power of PD appropriates −4 dBm. Simulation results are given in Figure 5. The fifth-order sidebands become the second dominant components in the optical domain and the OSSR is 13 dB. For the generated electrical signal, the RFSSR is limited by the sixth-order harmonic component and it is about 26 dB.

The MI is set as 3.999, the time delay of the TODL is still set as 11/80 ns. As the optical power output from DPMZM1 is high, thus just one EDFA is needed and placed after the DPMZM2, the gain of the EDFA is 15 dB and the noise figure is 4 dB. The average receiving optical signal power of PD appropriates −4 dBm. Simulation results are given in Figure 6. The third-order sidebands become the second dominant components in the optical domain, and the OSSR is 20 dB. For the generated electrical signal, the RFSSR is limited by the sixth-order harmonic and it is about 40 dB.

(a) (b)

Figure 5. (a) Optical, (b) electrical spectrum when m = 2.672.

(a) (b)

Figure 6. (a) Optical, (b) electrical spectrum when m = 3.999.

It can be seen from Figures 3-6 that the simulation results agree well with the theoretical analysis. Frequency 16-tupling mm-wave signals are generated with RFSSRs about 40 dB, 26 dB and 19 dB when m = 3.999, 2.672 and 2.405 respectively.

The generation of the mm-wave signal is achieved by adjusting the voltage of the oscillator, the phase difference between the driving signal, the time delay of the TODL, and the DC bias of the modulators. For the practical application, these parameters are not ideal, and they may degrade the performance of the proposed scheme. The influence of imperfect factors on the performance of OSSR and RFSSR for the generated mm-wave signal will be discussed in this part.

Figure 7 shows the simulation results of the OSSR and RFSSR against the power split ratio of the sub-MZM. The range of the extinction ratio of sub-MZM is 20 - 50 dB. The OSSR has a linear relationship with the extinction ratio as shown in Figure 7(a). The RFSSR increases along with the increase of extinction ratio firstly, because the undesired components are suppressed better when the extinction ratio is higher. Then the RFSSR retains unchanged when the extinction ratio is high enough, because the undesired components are lower than the noise power and the RFSSR is restricted by the noise. It also can be seen that, when the extinction ratio is given, a better performance can be obtained when a higher MI is provided.

Figure 8 shows the simulation results of the OSSR and RFSSR against the bias drift of the sub-MZMs when the extinction ratios are 30 dB. The bias voltage deviation ratio is defined as (ΔV/V_π) × 100%, where ΔV is bias voltage deviation. About 3 dB OSSR degradations are observed with 2% bias drift. The RFSSRs are more sensitive to the bias drift. When m = 3.999, a degradation of 26 dB is observed with 2% bias drift, but the RFSSR can be higher than 17 dB when the bias voltage deviation ratio is controlled within ±2% using bias feedback control circuit.

Figure 9 shows the simulation results of the OSSR and RFSSR against the imperfect phase delay of the PS with varying phase deviation from −2 to 2 degree.

(a) (b)

Figure 7. (a) OSSR, (b) RFSSR versus extinction ratio.

(a) (b)

Figure 8. (a) OSSR, (b) RFSSR versus bias deviation.

(a) (b)

Figure 9. (a) OSSR, (b) RFSSR versus phase deviation of PS.

If the phase deviation is smaller than ±1.5 degree, there are no significant degradations for OSSRs. Note that the maximal OSSR with m = 3.999 does not correspond to the desired phase difference, because the OSSR is not only depended on the phase difference, but also the extinction ratio. In the electrical domain, the phase deviation obviously degrades the RFSSR. When the phase deviation ranges from −2 to 2 degree, the RFSSRs degrade form 40 dB to 14 dB, from 26 dB to 6 dB, and from 19 dB to zero when m = 3.999, 2.672 and 2.405 respectively.

Figure 10 shows the simulation results of the OSSR and RFSSR against the RF driving voltage deviation when the extinction ratios of sub-MZMs are 30 dB. The normalized RF voltage deviation is defined as (ΔV_pp/V_pp) × 100%, where ΔV_pp is the RF driving voltage deviation. If the normalized RF voltage deviation is smaller than ±1%, there are no significant degradations for OSSRs, but degradations of 26 dB, 20 dB and 14 dB are observed for RFSSRs with m = 3.999, 2.672 and 2.405 respectively.

Finally, we give a comprehensive comparison of the four conditions that are used to generate a 16-tupling mm-wave signal. Assuming that the half-wave voltage of sub-MZM is 4.5 V, then the microwave power of LO for different MIs can be calculated as shown in the Table 1. The power penalty of optical system

(a) (b)

Figure 10. (a) OSSR, (b) RFSSR versus RF voltage deviation of PS.

Table 1. Power comparison of the four conditions with different MIs.

means that, when no EDFA is used, the optical power loss between the output of DPMZM2 and the output of LD, and they are estimated by the simulation results. The power compensation of optical amplifier means the gains needed in the simulation to guarantee the average receiving optical signal power of PD appropriates −4 dBm. It can be seen that when m = 3.999, the power of LO is 3 dB - 5 dB higher than the other three cases, but the power penalty of optical system is 20 dB - 30 dB lower.

4. Conclusion

A filterless frequency 16-tupling optical mm-wave signal generation approach is demonstrated. Compared with the reference [15], this paper gives a generalized investigation of the two cascaded DPMZMs scheme. Different MIs can be implemented to achieve the frequency 16-tupling signal by adjusting the delay of TODL. It is confirmed by simulation that the proposed scheme is effective. Influencing factors such as extinction ratio, DC bias drift, PS deviation and RF voltage deviation on the performance of OSSR and RFSSR are investigated. The simulation results show that the RFSSR of the generated frequency 16-tupling signal can be as high as 40 dB when the sub-MZMs have extinction ratios of 30 dB. Compared with the previous high-frequency multiplication factor schemes proposed in references [13] [15], the cascaded DPMZMs approach is more practical for application, because the value of MI is 2.405, 2.672 or 3.999, which is much lower than the previous schemes as 5.520, 8.654 or 9.761.

Acknowledgements

This work was supported by the National Natural Science Foundation of China (61901507).

Conflicts of Interest

The authors declare no conflicts of interest regarding the publication of this paper.

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