Research Article | Open Access
Santosh Vema Krishnamurthy, Kamal El-Sankary, Ezz El-Masry, "Noise-Cancelling CMOS Active Inductor and Its Application in RF Band-Pass Filter Design", International Journal of Microwave Science and Technology, vol. 2010, Article ID 980957, 8 pages, 2010. https://doi.org/10.1155/2010/980957
Noise-Cancelling CMOS Active Inductor and Its Application in RF Band-Pass Filter Design
A CMOS active inductor with thermal noise cancelling is proposed. The noise of the transistor in the feed-forward stage of the proposed architecture is cancelled by using a feedback stage with a degeneration resistor to reduce the noise contribution to the input. Simulation results using 90 nm CMOS process show that noise reduction by 80% has been achieved. The maximum resonant frequency and the quality factor obtained are 3.8 GHz and 405, respectively. An RF band-pass filter has been designed based on the proposed noise cancelling active inductor. Tuned at 3.46 GHz, the filter features total power consumption of 1.4 mW, low noise figure of 5 dB, and IIP3 of −10.29 dBm.
Inductors, either passive or simulated by active devices are key components in Radio Frequency Integrated Circuits (RFIC) analog building blocks such as filters , oscillators , phase shifters , and low-noise amplifiers (LNA) . As integrated circuit technologies are progressing, the usage of passive inductors is degrading due to their large chip area, low-quality factor, and less tunability. Mainly the inductor is the major chip area consuming building block ; the higher the inductance required, the higher the chip area. While tunability can be implemented using passive inductor and low-resistance switches, continuous tuning is not easily achieved. Due to these disadvantages, the concept of active inductors is becoming more attractive.
Many proposed active inductor architectures using MOS transistors [1–5] can be found in the literature. Higher noise, nonlinearity and power consumption are the major disadvantages of active inductors due to the fact that these circuits are realized using active devices which have higher noise. Thermal noise cancelling (NC) has been successfully implemented in LNA circuits by cancelling the noise of their input transistors [6, 7]. In this paper, NC is applied to active inductor architecture. First the transistor contributing most of the noise of the active inductor is identified in the forward path of Gyrator-C structure, and its noise contribution is cancelled using the feedback path while the noise contribution of the latter to the input is degenerated by the inclusion of shielding resistor in the feedback. NC allows active inductors to be used in applications such as front-end active RF filter in receivers and also to design low-phase noise oscillators.
The paper is organised as follows. In Section 2, the NC active inductor is presented, as well as the principle of NC and simulation results. In Section 3, a differential second-order RF band-pass filter based on the proposed NC active inductor and its performance are demonstrated. Finally, the conclusion is given in Section 4.
2. NC Active Inductor Design
In the active inductor circuit shown in Figure 1(a), is identified as the transistor with the highest noise contribution.
2.1. Noise Contribution of the Transistor
The circuit used to implement NC in active inductor is the Gyrator-C structure proposed in  and shown in Figure 1(a). In order to apply NC, we studied the noise contribution of each transistor and identified the transistor that has the highest percentage of noise to the total input referred noise. Usually in LNA, noise cancelling is applied to the input transistor. This is not the case of active inductors, and due to the back-to-back structure a careful study is needed to identify the transistor that contributes the highest noise at the frequency of interest.
The noise current of is modelled as the current source , between nodes 2 and 3 in Figure 1(a). For better understanding, we have shown the noise of as two current sources, one flowing out of node 3 and other flowing into node 2 . From noise analysis and simulation results, is found to be contributing more than 25% to the input noise at high frequency. The reason behind this high noise contribution is that the noise of will be amplified by the gains from the nodes 2 and 3 when referred to the input. These gains depend on the impedance at nodes 2 and 3 divided by the respective gains calculated from input node 1 to the nodes 2 and 3. As shown in Figure 1(b), the output impedance to the gain ratios go higher as frequency increases. Thus the noise current of multiplied by these two ratios to be referred to the input goes higher as frequency increases.
The input referred noise from nodes 2 and 3 can be calculated by breaking the feedback from drain of to the input. The input referred noise contribution from node 3 is calculated as Hence, Similarly, we can obtain the input referred noise from node 2 as where are the input referred noise currents of from nodes 2 and 3, respectively. are noise currents of at nodes 2 and 3, is the closed loop resistance at node 3, is the open loop resistance at node 3, is the closed loop transimpedance gain from node 1 to node 3 for the shunt-shunt feedback circuit in Figure 1(a), is the open loop transimpedance gain from node 1 to node 3, and is the feedback factor.
Equations (2) and (3) reveal that the noise contribution of goes higher at high frequencies. This can be understood from the fact that the Gyrator structure in Figure 1(a) has shunt-shunt feedback structure and the capability of this feedback topology to lower the output impedances at nodes 2 and 3 is reduced at higher frequencies due to the feedback forward gain reduction. That leads to higher contribution of the noise sources when multiplied by these output impedances at nodes 2 and 3 to be referred to the input at node 1.
2.2. NC Principle and Simulation Results
Figure 2 illustrates the modification introduced for cancelling the noise of ( is neglected at this time and nodes 1 and 4 are shorted). The noise current of , which is modelled as the current source , flows into node 2 but out of node 3 as shown in Figure 2. This creates two fully correlated noise voltages at nodes 2 and 3 with opposite phases. These two voltages are converted into current by and respectively. By properly matching the AC currents of and around the resonant frequency, the noise contributed by can be cancelled at the input.
Conversely, the signal voltages at nodes 2 and 3 are in phase, resulting in constructive addition at node 1. The condition for complete noise cancelling of can be derived as where is the total noise current of the entire 2nd stage, are the closed loop impedance and gain at node 4, are the open loop impedance and gain at node 4 and is the gain contributed from and . From (7), it is evident that increasing shields the input node of the active inductor from the noise contribution of the second stage formed by , and . Figure 5 shows the simulated noise contribution of the second stage when compared with and without . Figure 5 shows the noise contribution of second stage to the total input referred noise. Here we can see that by adding the noise contribution of 2nd stage has been reduced to 15% from 45%.
2.3. Active Inductor Parameters
In this section, the different parameters of the proposed active inductor are derived. The simplified active inductor is shown in Figure 6. The Gyrator-C principle on which active inductor is based on is depicted in Figure 7(a) and its equivalent passive model is shown in Figure 7(b). The differential pair and forms the positive transconductance with input node at 1 and output nodes at 2 and 3. The transistor pair and forms the negative transconductance with input nodes at 2 and 3 and output node at 1. These two blocks convert the parasitic capacitors at nodes 2 and 3 to an equivalent inductor appearing at node 1. The ideal current sources in the active inductor are implemented using simple current mirror.
The equivalent can be obtained from the small signal analysis circuit in Figure 8. For better intuition, a few parasitic parameters have been ignored. The approximate expression for is as follows: where denotes and denotes , and are the transconductances of transistors , are the total parasitic capacitances and conductances at nodes 1–4, is the conductance of feedback resistor, , and the cubic term in the denominator is substituted to , because the effect of negative real pole arising due to cubic term is of second order  when compared to dominant conjugate poles.
From (8), is equivalent to the input impedance of the RLC passive network shown in Figure 7(b). The passive equivalent elements are obtained as where is the series resistor with and the parallel parasitic capacitor are given by The resonant frequency is given by The quality factor at the resonant frequency is obtained as
The simulated frequency response of the active inductor is shown in Figure 9. The simulations are carried out in 90 nm STM CMOS process. The transistor sizes (W/L in m) are (6/0.18), (6/0.18), (11.5/0.18), (2.3/0.18), , , and . The active inductor resonates at centre frequency of with a quality factor of . The pole-zero analysis performed using Spectre simulator shows that all the poles reside on the left side of the axis and consequently the active inductor is stable. Also varying the feedback resistor (from 0 to 30 k) and and (by varying the active inductor biasing currents and from 300 A to 500 A) was applied to confirm the stability of the active inductor in case of tuning its center frequency and quality factor. Figure 10 shows the zero-pole plot for the active inductor transfer function while changing from 0 to 15 k. Moreover, transient analysis has been performed to confirm the stability.
Table 1 compares the performance of the proposed active inductor with the previously published active inductors [1, 9, 10]. Comparison of performances proves that this inductor has a good quality factor, wide inductive bandwidth, low-power consumption of 1.2 mW, and very less noise when integrated over 500 MHz bandwidth.
3. RF Band-Pass Filter and Simulation Results
Figure 11 shows the proposed pseudo-differential RF Band-pass filter implemented using proposed NC active inductor. The input stage is designed by the common-gate transistor which is biased by and . A source follower stage is used as an output buffer for output matching and to reduce the loading effect.
The effect of NC is high lightened by comparing the performance of the two band-pass filters. One designed using the active inductor with NC and other using the active inductor without NC (the transistor is turned OFF as mentioned above). In Figure 12, we can see that when the gain and centre frequency of the proposed band-pass filter are same, the NF without and with NC are 17 dB and 5 dB, respectively. And also we can see that when the 2 filters are tuned to have same quality factor and centre frequency, the NF without and with NC are 17 dB and 5.7 dB, respectively.
Figure 13 shows the filter NF and frequency response under extreme cases of combined process and mismatch variations. We can see that the NF has changed by almost 0.75 dB around the centre frequency while the gain of the filter has been changed without much variation in the centre frequency. The gain of the filter can be retrieved by tuning using the biasing current in Figure 11.
The linearity of the band-pass filter was examined by plotting the third-order intercept point (IIP3) using periodic steady state simulation as shown in Figure 14. The conditions for simulating the linearity are center frequency and the two signals injected were at frequencies of 3.48 GHz and 3.49 GHz, respectively. While noise cancelling reduces the noise floor, the harmonic distortion is not reduced as a result of NC conditions, which leads to almost constant dynamic range for the filter with and without NC. However, the harmonic distortion can be cancelled by selecting different conditions other than the one used for NC, therefore, simultaneous cancellation of noise and distortion is hampered . Despite the fact that this filter presents an acceptable linearity, the latter can be improved by increasing the overdrive voltages of transistors at the cost of higher power supply. Moreover, distortion cancelling techniques such as the one presented in  can be adapted to cancel the distortion of the proposed active inductor and that to improve the overall linearity of the designed RF filter.
Table 2 compares the performance of the band-pass filter using the proposed active inductor with previously published RF band-pass filters. Comparison of performances proves that this filter features lower-power consumption of 1.4 mW and lower noise figure of 5 dB at the filter centre frequency.
A 3.8 GHz noise cancelling CMOS active inductor is presented. The proposed active inductor has low noise due to noise cancelling and resistive degeneration. The circuit has wide inductive bandwidth, high-resonant frequencies with high-quality factor. Simulation results are provided in 90 nm 1.2 V STM CMOS process. A second-order band-pass filter has been designed based on this proposed active inductor. The designed filter including the input and output buffer stages has low NF and low-power consumption which makes it suitable for front-end RF filtering applications.
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Copyright © 2010 Santosh Vema Krishnamurthy et al. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.