What you need to know about transimpedance amplifiers – part 1

Transimpedance amplifiers (TIAs) act as front-end amplifiers for optical sensors such as photodiodes, converting the sensor’s output current to a voltage. TIAs are conceptually simple: a feedback resistor (RF) across an operational amplifier (op amp) converts the current (I) to a voltage (VOUT) using Ohm’s law, VOUT = I × RF. In this series of blog posts, I will show you how to compensate a TIA and optimize its noise performance. For a quantitative analysis of a TIA’s key parameters, such as bandwidth, stability and noise, please see the application note, ““Transimpedance Considerations for High-Speed Amplifiers.”

In a physical circuit, parasitic capacitances interact with the feedback resistor to create unwanted poles and zeros in the amplifier’s loop-gain response. The most common sources of parasitic input and feedback capacitances are the photodiode capacitance (CD), the op amp’s common-mode (CCM) and differential input capacitance (CDIFF), and the circuit-board capacitance (CPCB). The feedback resistor, RF is not ideal and has a parasitic shunt capacitance that may be as large as 0.2pF. In high-speed TIA applications, these parasitic capacitances interact with each other and RF to create a response that is not ideal. In this blog post, I will illustrate how to compensate a TIA.

Figure 1 shows a complete TIA circuit with parasitic-input and feedback-capacitance sources.

Figure 1: TIA circuit including parasitic capacitances

Three key factors determine the bandwidth of a TIA:

  • Total input capacitance (CTOT).
  • Desired transimpedance gain set by RF.
  • The op amp’s gain-bandwidth product (GBP): the higher the gain bandwidth, the higher the resulting closed-loop transimpedance bandwidth.

These three factors are interrelated: for a particular op amp, targeting the gain will set the maximum bandwidth; conversely, targeting the bandwidth will set the maximum gain.

Single-pole amplifier with no parasitics

The first step of this analysis assumes an op amp with a single pole in the AOL response and the specifications shown in Table 1.

Table 1: TIA specifications

An amplifier’s closed-loop stability is related to its phase margin, ΦM, which is determined by the loop-gain response defined as AOL × β, where β is the inverse of the noise gain. Figures 2 and 3 show the TINA-TI™ circuits to determine the op amp’s AOL and noise gain, respectively. Figure 2 configures the device under test (DUT) in an open-loop configuration to derive its AOL. Figure 3 uses an ideal op amp with the desired RF, CF and CTOT around it to extract the noise gain, 1/β. Figure 3 excludes parasitic elements CF and CTOT – for now.

Figure 2: DUT configuration to determine AOL

Figure 3: Ideal amplifier configuration to determine noise gain (1/β)

Figure 4 shows the simulated magnitude and phase of loop gain, AOL and 1/β. Since 1/β is purely resistive, its response is flat across frequency. The loop gain is AOL(dB) + β(dB) = AOL(dB), since the amplifier is in a unity-gain configuration as shown in Figure 3. The AOL and loop-gain curves thus lie on top of each other, as shown in Figure 4. Since this is a single-pole system, the total phase shift due to the AOL pole at fd is 90°. The resulting ΦM is thus 180°-90° = 90°, and the TIA is unconditionally stable.

Figure 4: Simulated loop gain, AOL and 1/β for an ideal case

Effect of input capacitance (CTOT)

Let’s analyze the effect of capacitance at the amplifier’s inputs on loop-gain response. I’ll assume a total effective input capacitance, CTOT, of 10pF. The combination of CTOT and RF will create a zero in the 1/β curve at a frequency of fz = 1/(2πRFCTOT) = 100kHz. Figures 5 and 6 show the circuit and resulting frequency response. The AOL and 1/β curves intersect at 10MHz – the geometric mean of fz (100kHz) and the GBP (1GHz). A zero in the 1/β curve becomes a pole in the β curve. The resulting loop gain will have a two-pole response, as shown in Figure 6.

The zero causes the magnitude of 1/β to increase at 20dB/decade and intersect the AOL curve at a 40dB/decade rate of closure (ROC), resulting in potential instability. The dominant AOL pole at 1kHz results in a 90° phase shift in the loop gain. The zero frequency, fz, at 100kHz adds another 90° phase shift. Its effect is complete by 1MHz. Since the loop-gain crossover occurs at only 10MHz, the total phase shift from fd and fz will be 180°, resulting in ΦM = 0° and indicating that the TIA circuit is unstable.

Figure 5: Simulation circuit including a 10pF input capacitor

Figure 6: Simulated loop gain, AOL and (1/β) when including the effects of input capacitance

Effect of feedback capacitance (CF)

To recover the phase loss due to fz, insert a pole, fp1, into the 1/β response by adding capacitor CF in parallel with RF. fp1 is located at 1/(2πRFCF). To get a maximally flat, closed-loop Butterworth response (ΦM = 64°), calculate CF using Equation 1:

where f-3dB is the closed-loop bandwidth shown in Equation 2:

The calculated CF = 0.14pF and f-3dB = 10MHz. fz is located at ≈7MHz. The feedback capacitor includes the parasitic capacitances from the printed circuit board and RF. In order to minimize CPCB, remove the ground and power planes beneath the feedback trace between the amplifier’s inverting input and output pin. Using resistors with small form factors, such as 0201 and 0402 reduces parasitic capacitance caused by the feedback components. Figures 7 and 8 show the circuit and resulting frequency response.

Figure 7: Simulation circuit, including a 0.14pF feedback capacitor

Figure 8: Simulated loop gain, AOL and 1/β when including the effects of input and feedback capacitance

Using Bode-plot theory, Table 2 summarizes the points of inflection in the loop-gain response.

Table 2: Effect of poles and zeros on the loop-gain magnitude and phase

The 1/β curve reaches a maximum value of  . For a Butterworth response, 1/β intersects AOL near its maximum value at a frequency   . fd and fz create a total phase shift of 180°. The phase reclaimed by fp1 is  , which is very close to the simulated 65°.

When designing a TIA, you must know the photodiode’s capacitance, as this is usually fixed by the application. Given the photodiode capacitance, the next step is to select the correct amplifier for the application.

Choosing the right amplifier requires an understanding of the relationship between an amplifier’s GBP, the desired transimpedance gain and closed-loop bandwidth, and the input and feedback capacitances. You can find an Excel calculator incorporating the equations and theory described in this post here. If you are designing a TIA, be sure to check the calculator out. It will save you a lot of time and manual calculations.

Additional resources

  • Hi,

    Could you explain the following

    1) Why the source resistance is not considered while calculating the loop gain or Noise gain

    2) Can the differential input capacitance be neglected due to virtual ground behavior as explained in your previous post ?

  • This post is referred to by the latest decomp parts for transimpedance design - it gives the correct Cf solution for a butterworth design including the 0.707 term. The added resources though. The first is the the one by Xavier Ramus from my original work and I am sure it is correct. However the 4th reference on choosing the best amplifier by Hooman repeats a common error in setting the Cf - essentially targeting the feedback pole at the Fo frequency - this will give you a closed loop Q=1 peaking, where as the correct equation gives you butterworth. Might want to edit that older app note by Hooman or remove it.