TABLE OF CONTENTS
Page
ABSTRACT . iii
DEDICATION . v
ACKNOWLEDGEMENTS . vi
TABLE OF CONTENTS . vii
LIST OF FIGURES . ix
LIST OF TABLES . xiii
CHAPTER
I INTRODUCTION 1
II BASIC VGA STRUCTURES . 4
II.1 VGA structures . 4
II.1.1 Differential pair with diode-connected loads . 4
II.1.2 Analog multiplier . 12
II.1.3 Differential pair with source degeneration . 16
II.1.4 Complementary differential pairs with source
degeneration . 17
II.2 Comparison of the commonly used VGA structures 20
III PROGRAMMABLE CURRENT MIRROR 22
III.1 Review of simple current mirror 22
III.2 Proposed programmable current mirror 24
III.2.1 AC response of programmable current mirror 29
III.2.2 Programmability of the programmable current mirror . 35
III.3 Conclusions . 36
IV DESIGN CONSIDERATIONS OF THE PROPOSED VGA 38
IV.1 VGA design challenges and motivations 38
IV.2 System-level overview of the proposed VGA s 39
IV.2.1 System-level design of the proposed VGA 39
IV.2.2 Introduction of the building blocks of the proposed VGA 40
IV.3 Detailed discussion of the VGA building blocks 43
CHAPTER Page
IV.3.1 Gain control scheme . 43
IV.3.2 Input stage complementary differential pairs with source
degeneration . 47
IV.3.3 Current gain stage—programmable current mirror 49
IV.3.4 Frequency compensation scheme . 51
IV.3.5 DC offset cancellation 57
IV.3.6 Digital control circuit 57
IV.3.7 The dimension and bias current for the VGA . 58
IV.4 Conclusion . 59
V SUMMARY OF RESULTS . 60
V.1 Design summary . 60
V.2 Simulation setup . 60
V.3 Simulation results . 63
V.3.1 Explanation of simulation terminologies . 63
V.3.2 Layout 67
V.3.3 AC response . 68
V.3.4 Noise 73
V.3.5 Linearity . 75
V.3.6 Power consumption 77
V.4 Experimental results . 77
V.4.1 Experimental results for the AC response of the VGA 79
V.4.2 Experimental results of the IIP3 . 86
V.4.3 Noise characterization 88
V.5 Summary of results and comparison 92
VI CONCLUSION . 95
REFERENCES 97
APPENDIX A . 99
APPENDIX B 102
VITA 107
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n
out
CCR
s
C
g
s
CC
R
g
s
CCC
CCg
i
i
+
+
+
+
+
+
+
+
≅
311
1
31
1
311
312
5.0
1
2
1
2
(4.5)
With the Cadence simulation, the f
-3dB of the multi-stage programmable current
mirror vs. the current gain can be plotted as shown in Fig 4.8. The simulation setup is
shown in Fig 4.7. The dimensions and the bias current values are the same as listed in
50
Table 3.3. Notice that for an M-stage programmable current mirror to obtain a total
current gain of L, each current gain M LN = .
Fig 4.7 Simulation setup for multi-stage programmable current mirror
Fig 4.8 shows that with two or more programmable current mirror stages, to
implement current gain of 5 A/A, their f
-3dB all drop to less than 700MHz. Including the
parasitic capacitance from the input stage which is also connected to the diode-
connected node of the programmable current mirror, the overall f
-3dB of the VGA may
fall below the design requirement (>350MHz). Thus, to ensure enough bandwidth at a
large gain variation, only one-stage programmable current mirror is chosen in this
design. The details about the programmable current mirror are given in Chapter III.
51
Fig 4.8 f
-3dB of the multi-stage programmable current mirror
vs. current gain
IV.3.4 Frequency-compensation scheme
To ensure that even with all parasitic included the overall bandwidth of the VGA
is still enough to meet the requirement, the frequency compensation is implemented. To
explain the concept of this compensation and its effectiveness, we refer to the
programmable current mirror in Fig 4.9.
52
Fig 4.9 Simplified schematic of the programmable current mirror
From equation 3.15, and there are two poles in the programmable current mirror:
( ) ) nodeat (5.0
1
,) node(at
2 31
2
1
1
1 DCCR
C
C
g
P
m
P
+
== ωω .
11333221111 and 2 where SBGSDBGDGDGSDBGDGS CCCCCCCCCCC +++=++++=
We can cancel some parasitic capacitance at node C. The capacitive frequency
compensation is shown in Fig 4.9. At node Vo, ignoring the output resistance of
compensation transistor:
( )
( )
C
m
m
mCm
Cm
in
o
m
XCoXminXmo
C
g
s
sg
sCCg
sCg
V
IG
sVCIsVCVVgI
+
−≈
++
−==
==+−+ and 0
(4.6)
53
Fig 4.10 Single-ended version of the compensation circuit and its
small signal model
So this is equivalent to a negative capacitor (-CC) and a negative resistor (-1/gm)
connected in series to node C. This gives us a high-pass characteristic as shown in Fig
4.11.
54
(a) (b)
Fig 4.11 Compensation effects on the current mirror
As illustrated in Fig 4.11 (b), there exists a corner frequency gm /CC. If the corner
frequency is higher than the frequency of the pole at node C, we should move this corner
frequency to lower frequency to compensate the poles in our VGA. To reduce it, we can
either increase CC or reduce gmc. In Figs 4.12 and 4.13, it is shown that increasing Cc
and reducing gmc in a certain range, the bandwidth of the VGA is extended to higher
frequency. But if we further reduce the corner frequency of the compensation to lower
than the frequency of the pole at node C, the overall capacitance at that node becomes
negative. It results in large peaking and extremely large group delay variation. So, the
negative capacitance effects from our compensation scheme should not over-compensate
the positive parasitic capacitance there.
55
Fig 4.12 Capacitance variation effects on frequency response
Fig 4.13 gmc variation effects on frequency response
56
Fig 4.12 shows that by increasing compensation capacitor values from 120 to
240pF, the bandwidth of the VGA is extended. When the capacitor value reaches beyond
200pF, the group delay variation is larger than 200pS which is not tolerable by our
design requirement. Therefore, the compensation capacitor should not be increased
above certain level, and this level is restricted by the group delay variation requirement.
Fig 4.13 indicates that by decreasing the transconductance of the transistor Mc, the
bandwidth of the VGA can be extended. However, by further decreasing it to under a
certain level, the group delay variation will be intolerable too as shown in Fig 4.12.
Therefore, observe from Figs 4.12 and 4.13 that restricting by the group delay variation
requirement (<200pS), the compensation will extend the f
-3dB by approximately 50%.
Because our VGA is in fully differential style, the capacitive frequency
compensation is implemented in a differential version as well (see Fig 4.14 and Table
4.5).
Fig 4.14 Implementation of the capacitive frequency compensation
57
Table 4.5 Dimension of the capacitive frequency compensation
Ibias WMc CC
220µA 12µm 160fF
IV.3.5 DC offset cancellation
To fix the DC operating point at the output between M3 and M6, and to cancel out
common-mode offset, an offset-cancellation circuit is used, as illustrated in Fig 4.3. M4
is half of the size of M3, (W/L)M4 = 1/2(W/L)M3, and M5 and M6 are identical. So the AC
signals at A and B are cancelled, and only their common-mode DC values are left and
are feedback to M6 and M3. Because of the size used here, the feedback DC current is
exactly the amount needed to correct the operating point of M6 and M3 to its ideal level.
Through this approach, disregarding how the DC bias current changes in the input stage,
the output DC level is fixed.
IV.3.6. Digital control circuit
According to the discussion in the gain control scheme, there are 3 steps of
coarse tuning and 8 steps of fine tuning. Hence, we can use 2-bit digital control for the
coarse tuning and 3-bit digital control for the fine tuning, as illustrated in Fig 4.4. From
Table 3.2, the digital gain control for the bias voltage of M2 in Fig 3.4 is identical to the
thermometer code, the logic for which is given as:
( )
21062152104
3321022112100
bbbsbbsbbbs
bsbbbsbbsbbbs
++=+=+=
=+===
(4.7)
58
Then, the digital control circuit is implemented, as in Fig 4.15.
Fig 4.15 Digital control circuit
IV.3.7 The dimension and bias current for the VGA
The nominations of the components in the VGA are illustrated in Figs 4.2 and
4.3. The corresponding dimensions and bias currents for the VGA are shown in Tables
4.6 and 4.7. Please refer to Appendix B for the calculation details.
Table 4.6 Dimensions and bias currents of the components of the VGA in the signal path
WMp WMn Rs1 Rs2 Rload
78um 78um 3K ohmRsn1
4.5K ohmRsn1
300 ohmRsn2
450 ohm(Rsn2)
1.5K ohm
Ibias Ib WM1 WM2 WM3
400µA 220µA 24µm 16µm 24µm
L = 0.24um for all transistors
59
Table 4.7 Dimensions for the transistors in the bias control circuit (Fig 4.3)
WMb1 WMb2 WMb3 WMb4 WMb5 WMb6 WMb7
2µm 4.8µm 4.8µm 4.8µm 4.8µm 1.68µm 0.72µm
IV.4 Conclusion
In this chapter, the design challenges and motivations of this VGA design are
summarized. Complementary differential pairs with source degeneration are used as the
input stage to achieve the good power-efficiency and maintain enough linearity. The
programmable current mirror is proposed as the current amplification to further amplify
the current, which has good programmability and frequency response. To cover the large
variable gain range, gain tuning is further divided into coarse and fine tuning. Coarse
tuning is obtained by changing the source degeneration resistor in the input stage; while
fine tuning is achieved by varying the transistor dimension in the bias control circuit and
hence changing the current amplification ratio. Both schemes are programmed by the
digital gain control. Capacitive frequency compensation is adapted to further extend the
bandwidth of the VGA, and a DC offset cancellation is used to fix the DC output voltage
level and cancel out the offset voltage due to gain changing or mismatch effects. Overall,
the proposed VGA structure is able to achieve large variable gain rang, very large
bandwidth with very low power consumption, and very small group delay variation. The
simulation result of this design will be given in the next chapter to justify the
performance of this VGA.
60
CHAPTER V
SUMMARY OF RESULTS
The VGA has been designed in the IBM 6HP 0.25µm CMOS process.
Simulation results are included in this chapter. The experimental results for the prototype
fabricated in the same process are presented.
V.1 Design summary
The design specifications for the VGA are summarized in Table 5.1.
Table 5.1 Design specifications for VGA
Technology IBM6HP 0.25µm CMOS process
Variable gain range 0 ~ 42dB, 2dB/step
Bandwidth (f
-1dB) > 264MHz
Linearity (IIP3) > -15dBm
Noise (Noise Figure) < 25dB
Group delay variation < 200pS
Power consumption < 20mW
V.2. Simulation setup
Two simulation setups are performed, these are:
61
1) Use a buffer to provide the voltage level shift for the ADC’s 0.3V input DC
voltage level. In this case, the load resistors are still chosen as the previous design value
which is 2K.
2) Without using a buffer to ADC while the VGA output is directly connected to
the output pads which have large capacitance (about 5pF). The load resistors are external
resistors outside the chip, and to ensure VGA’s bandwidth will not get degraded by the
pole from the resistance from the load and the large parasitic capacitance of the pads, the
load resistors are intentionally made accordingly smaller—100 ohm for this case .
(a) With buffer to ADC stage (Rload = 2K ohm)
(b) Without buffer to ADC stage (Rload = 100 ohm)
Fig 5.1 Simulation setup
62
Comparing these two setups, we realize that the maximum DC gain from the
second setup will be 16dB instead of 42dB because its load resistor is 20 times smaller
than that of the first case. However, it can be still verified the functionality of the VGA
based on the second setup, as the VGA current amplification range in both setups is the
equal, just the load resistor plays a multification factor to determine the final absolute
value of the gain. These two setups are shown in Fig 5.1.
The dimensions of the VGAs used in the different setups are listed in Table 5.2
as shown.
Table 5.2 Dimensions of the VGAs for different setups
With buffer to ADC stage
Mp Mn Rs1 Rs2 Rload M1 M2 M3
78/0.24
(µm)
78/0.24
(µm)
3K ohm
4.5K ohm
300 ohm
450 ohm
2K ohm 24/0.24
(µm)
16/0.24
(µm)
24/0.24
(µm)
Ibiasn* Ibiasp*
910µA 1040µA
Mb1 Mb2 Mb3 Mb4 Mb5 Mb6 Mb7
2/0.24
(µm)
4.8/0.24
(µm)
4.8/0.24
(µm)
4.8/0.24
(µm)
4.8/0.24
(µm)
1.68/0.24
(µm)
0.72/0.24
(µm)
Without buffer while directly connected to the output pads
Mp Mn Rs1 Rs2 Rload M1 M2 M3
78/0.24
(µm)
78/0.24
(µm)
3K
4.5K
300
450
100 As the same as the case with
buffer to ADC
Ibiasn* Ibiasp* Mb1 Mb2 Mb3 Mb4 Mb5 Mb6 Mb7
1170 µA 1040µA As the same as the case with buffer to ADC
63
In the following sections, the post-layout simulation results of these two setups
will be shown and discussed.
V.3 Simulation results
V.3.1 Explanation of simulation terminologies
The simulation results provided are collected from the post-layout simulations, in
which all the parasitic capacitors are extracted except for the well-to-subtract parasitic
capacitance. Measurement setting and simulated terms are defined as follows.
(1) -1dB bandwidth (f
-1dB)
This is the bandwidth in which the voltage gain is 1dB below the DC gain. It
indicates the gain flatness of the VGA within the useful bandwidth.
(2) -3dB bandwidth (f
-3dB)
This is the bandwidth in which the voltage gain is 3dB below the DC gain, and it
is commonly used as a critical specification in many VGA designs.
(3) Linearity and distortion
Consider a nonlinear system described by
)()()()( 332210 txatxatxaaty +++= (5.1)
where y (t) and x (t) are the output and input of the system respectively.
Consider ( ) ( )tAtAtx 21 coscos)( ωω += , where 1 and 2 are two frequencies
very closed to each others around the frequency of interest, substitute this into equation
5.1 yields
64
( ) ( ) ( ) ( )
( ) ( ) ( ) ( )[ ]
( ) ( )[ ] ( )[ ] ( )[ ]
( )[ ] ( )[ ]
( ) ( )tAatAa
t
Aa
t
Aa
t
Aa
t
Aa
tAa
tAatAatAa
t
AaAatAaAaAaaty
2
3
3
1
3
3
12
3
3
21
3
3
12
3
3
21
3
3
21
2
2
21
2
22
2
2
1
2
2
2
2
3
11
2
3
1
2
20
3cos
4
33cos
4
3
2cos
4
32cos
4
3
2cos
4
32cos
4
3
cos
cos2cos
2
2cos
2
cos
4
9
cos
4
9
ωω
ωωωω
ωωωωωω
ωωωω
ωω
+
++
++
+−
+−
+−
+++
+
+
++
+++=
(5.2)
The third-order intercept point (IIP3): It is defined as the input signal power level
at which the fundamental component intercepts with the third-order intermodulation
component. From equation 5.2,
( )
3
1
3
3
33
31 3
4
4
3
a
a
AAaAa IIPIIPIIP =
= (5.3)
Also, the third-order intermodulation distortion IM3 is defined as
2
1
3
4
3
3 A
a
a
IM = (5.4)
Comparing equation 5.3 and 5.4, we can relate IIP3 with IM3 as follows,
( ) ( )
2
)()()(
log20log20log20/
4
3
/
3
3
3
22
33
22
1
322
3
dBIMdBmAdBmA
IMAAIMAA
a
a
AA
IIP
IIPIIP
−=
−==
=
(5.5)
where A is the input signal magnitude in dBm unit.
By measuring IM3 at a certain input signal level, IIP3 can be obtained
accordingly.
65
(4) Input referred integrated noise
Input referred noise is the noise collected from the VGA output divided by the
gain of the VGA. In this simulation, the input referred integrated noise is integrated from
DC to 250MHz.
(5) Signal-to-Noise-Ratio (SNR)
Low noise is an important concern if the input signal is very small and the
bandwidth of interest is very wide. Since we are interested in a very high frequency, the
contribution from the 1/f noise at a lower frequency can be neglected. Signal-to-Noise-
Ratio is
2
,
2
,log10
inn
rmsin
V
V
SNR = (5.6)
where rmsinV , is the root-mean-square value of the input signal, and innV , is the equivalent
input referred noise voltage.
(6) Noise Figure (NF)
The most commonly accepted definition of Noise Figure is given in equation 5.7.
Noise
out
in
SNR
SNR
Figure = (5.7)
Noise Figure is a measure of how much the SNR degrades as the signal passes
through a system. And it can be written as:
⋅
+⋅=
BWkTR
INNF
s4
1log10
2
(5.8)
66
where IN is short for integrated input referred noise voltage.
For Rs = 50 and BW = 250MHz, 2101096.14 VBWkTRs −×=⋅
(7) Group Delay
The Group Delay is defined as the rate of change of the total phase shift with
respect to the angular frequency:
Group Delay =
ω
θ
∂
∂
(5.9)
It also is the time delay through the system for a sine wave pulse. If the group
delay is non-uniform and varies with the sine-wave frequency, the time-domain response
to a sharp input-signal change may show overshoot or ringing. Thus, a perfectly uniform
group delay is equivalent to a perfectly linear phase response.
(8) Figure of Merit (FOM)
A Figure of Merit (FOM) is defined such that this VGA’s performance can be
compared with other VGA designs fairly. Based on the design requirements, the FOM
should include the maximum DC voltage gain ( )0(
,MAXVA ), the -3dB frequency
bandwidth ( dBf 3− ), the technology, the power consumption, and the silicon area of the
VGA. With concerns of linearity and noise, the Signal to Noise Ratio should be included
in the FOM as well, which indicates the ratio between the input signal level (under
sufficient linearity level) and the input referred noise voltage. Thus, the FOM can be
defined as
67
AreaPower
TechnologySNR)0( 3,
×
×××
=
− dBMAXV fAFOM (5.10)
Next, the post-layout simulation results are presented in detail.
V.3.2 Layout
The VGA is laid out for I/Q channels, and includes analog and digital parts as
shown in Fig 5.2.
Each VGA occupies silicon area of 22 mm0154.0m15400m110m140 ==× ,
and the total area of I/Q channels is approximately 0.03mm2.
Fig 5.2 Layout view of the I/Q channels of the VGA
68
V.3.3 AC response
The VGA post-layout simulation results of the AC response are shown in Figs
5.3 through 5.8d. It achieves 0 to 42dB with 2dB/step for this VGA with both simulation
setups (one with a buffer to ADC and the other without). For the setup with a buffer to
ADC, it achieves f
-1dB > 321MHz (f-3dB= 474MHz), and the group delay for all cases is
less than 150 pS. As for the setup without a buffer with the VGA output directly tied to
the pads, it achieves f
-1dB > 290MHz (f-3dB= 411MHz), and the group delay for all cases
is less than 110 pS for all gain cases. Therefore, all results meet the requirements, as
summarized in Tables 5.3 and 5.4.
Table 5.3 Post-layout AC response simulation results vs. system requirements
With buffer to ADC Gain Range (dB) Bandwidth (MHz) Group Delay(pS)
Post-Layout
Simulations
321[f
-1dB] (474[f-
3dB])
146
System
Requirements
0 ~ 42dB
2dB/Step
>264 [f
-1dB] <200
Without buffer to
ADC
Gain Range (dB) Bandwidth (MHz) Group Delay(pS)
Post-Layout
Simulations
311[f
-1dB] (290[f-
3dB])
108
System
Requirements
0 ~ 42dB
2dB/Step
>264 [f
-1dB] <200
69
Table 5.4 AC response
a. With Buffer to ADC (Rload = 2K ohm)
2dB/Step, 0 ~ 42dB
Ideal Gain (dB) Real Gain (dB) f
-3dB (MHz) Group Delay(pS)
42 42.65 474 (321[f
-3dB]) 45
36 35.9 492 86
30 30.14 512 110
24 24.3 528 102
18 18.14 540 131
12 11.92 548 136
6 6.1 562 139
0 0.368 580 146
b. Without buffer to ADC (Rload = 100 ohm)
Ideal Gain (dB) Real Gain (dB) f
-3dB (MHz) Group Delay(pS)
16 16.65 411(290 [f
-3dB]) 39
10 10.8 432 44
4 4.3 459 67
-2 -1.4 489 93
-8 -7.3 490 89
-14 -13.9 496 96
-20 -20.4 512 102
-26 -26.3 520 108
70
(1) Frequency response based on VGA setup with buffer to ADC
Fig 5.3 Gain steps from 30dB to 42dB
Fig 5.4 Gain steps from 16dB to 28dB
71
Fig 5.5 Gain steps from 0dB to 14dB
(2) Frequency response based on VGA setup without buffer to ADC
Fig 5.6 Gain steps from 2dB to 16dB
72
Fig 5.7 Gain steps from -12dB to 0dB
Fig 5.8 Gain steps from -26dB to -14dB
73
V.3.4 Noise
(1) SNR
The Signal-to-Noise-Ratio (SNR) is defined previously in equation 5.6 as the
ratio between the root-mean-square values of the input signal to the corresponding
equivalent input-referred noise voltage.
2
,
2
,log10
inn
rmsin
V
V
SNR = (5.6)
where rmsinV , is the root-mean-square value of the input signal, and innV , is the equivalent
input referred noise voltage.
VGA with maximum gain setting has the smallest input signal. Therefore, noise
at a 42dB gain setting is characterized at this section. As the differential output-signal
level of the VGA is fixed to 1Vpp, and the equivalent input referred noise power ( 2,innV ) is
3.6×10-9V2/Hz at 42dB gain, so the SNR is given as
9
2
20
42
2
,
2
,
106.3
1022
1
log10log10
−
⋅
⋅
==
inn
rmsin
V
V
SNR = 33.4dB
(2) Noise Figure
The Noise Figure (NF) can be written as:
⋅
+⋅=
BWkTR
INNF
s4
1log10
2
(5.8)
74
where IN is short for Integrated Input Referred Noise Voltage.
For RS=50 ohm and BW = 250MHz, 2101096.14 VBWkTRS −×=⋅ . Thus, we
calculate the Noise Figure based on IN as shown in Fig 5.9. As expected, the Noise
Figure degraded from high-gain to low-gain cases as shown in Fig 5.9. The worst Noise
Figure for the VGA with a buffer to ADC is 18.7dB; while for the case without a buffer,
it gives 20.1dB for the worst case. So, both cases meet the system specification which
requires the Noise Figure to be less than 25dB for all gain steps.
Noise Figure for different gain
18.7
18.2
17
15.6
14.5
13.8
12.9 12.6
10
11
12
13
14
15
16
17
18
19
20
0 6 12 18 24 30 36 42 48
Gain levels (dB)
No
is
e
Fi
gu
re
(dB
)
(a) With buffer to ADC (Rload = 2K)
Fig 5.9 Noise Figure for different gain levels
75
Noise Figure for different gain
20.1
19
17.8
16.5
15.3
14.5
14
13.6
10
11
12
13
14
15
16
17
18
19
20
21
-26 -20 -14 -8 -2 4 10 16 22
Gain levels (dB)
No
is
e
Fi
gu
re
(dB
)
(b) Without buffer to ADC (Rload = 100)
Fig 5.9 Continued
V.3.5 Linearity
Because the output signal level is fixed by the VGA, increasing the gain in the
VGA corresponds to lower input signal level, which relaxes the linearity requirement of
the VGA. In other words, the most critical case to ensure good linearity in the VGA
should be the lowest gain case, which corresponds to the largest input signal level.
Therefore, the VGA should be designed to posses improving linearity when gain is
reduced; that is the reason more source degeneration resistance in the lower gain case are
76
turned on. IIP3 for different gain settings is plotted in Fig 5.10. As expected, the better
linearity is achieved in lower gain cases. The worst case for IIP3 is at 42dB, which is
-6.3dBm, and is better than the required -15dBm.
IIP3 for Different Gain Levels
21.1
18.6
11.3
4.25
-0.95
-4.85
-5.4
-6.3
-10
-5
0
5
10
15
20
25
0 6 12 18 24 30 36 42 48
Gain Levels (dB)
IIP
3
(dB
m
)
(a) With buffer to ADC (Rload = 2K ohm)
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Z
Z[
\
] ^
_ `
a
(b) Without buffer to ADC (Rload = 100 ohm)
Fig 5.10 IIP3 for different gain levels
77
V.3.6 Power consumption
The maximum power consumption happens at the highest gain case—42dB,
which only consumes 9.5mW and is way below the 20mW required by the system as
shown in Fig 5.11, because the power efficient complementary differential pairs are used
as the input stage.
Fig 5.11 Power consumption
V.4 Experimental results
Fig 5.12 VGA testing pins arrangement
78
Fig 5.13 VGA input/output testing setup
The testing setup is shown in Figs 5.12 and 5.13. The VGA is fabricated in IBM
6HP 0.25m CMOS technology. To convert single-ended input signal from the signal
generator to the differential inputs for the VGA, balun (an abbreviation for balanced to
unbalanced) is used. The ratio of the number of balun turns from single end to the
differential ports is 1:4. Because broadband matching is required, only resistive instead
of impedance-matching networks are used to match the output impedance of the signal
generator. To convert the differential output signal from the VGA into the single-ended
signal required by the measurement of the spectrum analyzer, a 4:1 balun is used at the
output of the VGA. The 47pF capacitors are used for the AC coupling so that the input
common-monde voltage is set by the input common-mode voltage level which is 1.25V
for this design, and the output common-mode voltage is fixed at the middle of the power
supply voltage to maximize the output voltage swing. For the measurement, a spectrum
79
analyzer with 50 ohm input impedance is used to measure the frequency response. The
supply voltage is 0 to 2.5V.
The testing shows a gain variation from -18dB to 14dB, with a 2dB/step.
Including the gain loss of approximately 2dB from the balun (transformer), the
maximum gain is as we expected as the post-layout simulation of 16dB for maximum
gain with a 100 ohm load resistor (with 2K ohm, it will be 42dB). The -1dB frequency is
from 266 to 293MHz, all above 264MHz, but a little bit short than the post-layout
simulation (288~ 315MHz). The IIP3 are closed to the post-layout simulation results too.
V.4.1 Experimental results for the AC response of the VGA
The results are listed and illustrated in Table 5.5 and the remaining figures in the
chapter. As mentioned previously, to avoid the bandwidth reduction caused by the pole
from the large parasitic capacitance of the pad and the load resistor, a 100 ohm resistor is
used as the load instead of 2K ohm. With this test setting, the experimental results show
a gain range from -18dB to 14dB with the 100 ohm load resistor. Including the gain loss
from the balun which is about 2dB, the above gain range corresponds to a gain range of
10 to 42dB with 2K ohm load resistor. We can also compare the DC gain of the testing
results with the ideal DC gain steps desired to get an idea of the accuracy of the gain
steps. In Table 5.5, it shows that, regarding the gain step accuracy, the worst case has a
0.73dB deviation from the ideal case (at -2dB ideal case, the experimental result shows -
1.2783dB). Thus, we can conclude that the deviations of gain-step from our desired
values are all within the 1dB range. This further justifies that the programmable current
80
mirror proposed in this design can be accurately controlled to provide the desired gain
variation at least to 2dB/step.
As for the bandwidth, the -1 dB bandwidth (f
-1dB) is defined previously to ensure
the gain flatness within the useful bandwidth. Hence, we desired to have f
-1dB at least
larger than 264MHz for all cases to cover the entire band of interest. Among all the gain
steps, the smallest f
-1dB is about 266MHz and the largest is about 293MHz. These results
verify that this design has enough bandwidth to cover the desired band and that the
bandwidth is relatively constant along the whole gain range. The large and constant
bandwidth is benefit from the good frequency response of the programmable current
mirror and the capacitive frequency compensation, as demonstrated in Chapter IV.
Besides, comparing to the post-layout simulation results, it can be also observed
that the deviations of the gain steps between the post-layout simulation and the
experimental results are all within the 2dB range, which indicates that the IBM 6HP
design-kit includes relatively accurate models of parasitic effects of the components and
thus provides designers a close estimation between the simulation results and the real
performance of the design on the silicon.
81
Table 5.5 Testing results for VGA AC response
Post-layout simulation Testing Gain steps
(dB) DC Gain (dB) f
-1dB (MHz) DC Gain (dB) f-1dB (MHz)
-18 -18.3 315 -18.687 291.15
-16 -15.92 310 -16.095 284.06
-14 -13.9 304 -14.273 282.4
-12 -12.1 320 -12.2 291.9
-10 -9.9 316 -10.068 291.105
-8 -7.3 305 -7.27 281
-6 -5.92 310 -5.6832 281.875
-4 -4.05 307 -4.168 288.56
-2 -1.4 298 -1.2783 276.68
0 0.24 303 -0.595 288.2
2 2.1 307 2.3413 293.57
4 4.3 305 4.2174 283.67
6 5.95 302 6.011 270
8 8.02 302 7.9052 267.87
10 10.8 294 9.108 270.48
12 11.78 299 11.492 270.22
14 13.85 288 13.561 266.7
The measurement results of the frequency response of the gain settings of 14, 12,
10, 8, and 6dB with a 100 ohm load resistor is shown in Fig 5.14. Including the loss
from the balun, which is about 2dB, this group of gain settings correspond to 42, 40, 38,
36, and 34dB with the 2K ohm load resistor. Because we are considering the whole
82
VGA gain range, this group of gains is high gain stages, the -1dB frequency of this
group of gain settings is between 266 to 270MHz as illustrated in Table 5.5 previously
and are relatively low compared to other low gain cases. Table 5.5 also shows that the
gain accuracy of this group of gains is below 0.9dB derivation from the ideal DC gain
values. This gain derivation is still tolerable because it is less than the minimum gain
step (2dB/step) of the VGA.
Fig 5.14 Frequency response of gain settings of 14, 12, 10, 8, and 6dB
The measurement results of the frequency response of the gain settings of 4, 2, 0,
-2, -4, and -6dB with a 100 ohm load resistor are shown in Fig 5.15, and correspond to
32, 30, 28, 26, 24, and 22dB with the 2K ohm load resistor. The -1dB frequency of this
83
group of gain settings are between 298 to 310MHz. The gain accuracy of this group of
gains is all below 0.73dB derivation from the ideal DC gain values, and this is tolerable
because it is still fall below the minimum gain step (2dB/step) of the VGA.
Fig 5.15 Gain setting of 4, 2, 0, -2, -4, and -6dB
The measurement results from the frequency response with the gain settings of -
8, -10, -12, -14, -16, and -18dB with a 100 ohm load resistor are shown in Fig 5.16, and
they correspond to 20, 18, 16, 14, 12, and 10dB with the 2K ohm load resistor. Their f
-
1dB frequency of this group of gain settings is between 305 to 315MHz, which is higher
than the rest gain settings because this is a low gain-stage group. Table 5.5 also shows
that the gain accuracy is below the 0.7dB derivation from the ideal DC gain values,
which is higher than the rest of the gain settings because this is a low gain-stage group.
84
Fig 5.16 Gain setting of -8, -10, -12, -14, -16, and -18dB
We couldn’t accurately measure the rest of the gain settings between -26 to -
20dB with a load resistor 100 ohm, which correspond to 0 to 8dB with load resistor of
2K ohm. One reason is that the chip included this VGA design has a malfunction in its
ESD protection pins, its ESD_VDD and ESD_GND are shorted together. This mistake
severely limits the control voltage range of the digital control circuit to be less than two
times the diode’s forward bias voltage (about 1.4V). In a result, some of gain stages may
miss if the digital circuit can not be fully turned on or off.
The measured frequency response of the maximum and minimum gain steps are
shown in Figs 5.17 and 5.18 respectively.
85
Fig 5.17 Gain setting of -18dB: Av(0) = -18.687dB, f
-1dB = 291.15MHz
Fig 5.18 Gain setting of 14dB: Av(0) = 13.561dB, f
-1dB = 266.7MHz
86
V.4.2 Experimental results of the IIP3
To measure the IIP3, the two-tone test is performed with one tone at 240MHz
and the other at 260MHz. By sweeping the input signal’s power level, two sets of data
are recorded. One set of data is for the output power level of the fundamental tone (at
240 and 260MHz), and the other set of data is for the output power level of the third
harmonic (at 220 and 280MHz) due to the intermodulation of the input two tones. By
recording several of those data at different input power level, the curve of the power
levels of the fundamental tones and the third harmonic tones changing along the varied
input signals can be obtained. Hence, using a straight line to interpolate these two
curves, the intersection point of the two curves can be found. The corresponding input
signal power level is the IIP3. The whole procedure is illustrated in Fig 5.19.
Fig 5.19 Measure IIP3 with interpolation
87
According to this measurement procedure, the IIP3 of different gain stages are
obtained as shown in Fig.5.19. The measured IIP3 of the maximum and minimum gain
steps are summarized in Table 5.6. Notice that, the balun (transformer) loss is about
2dB, and the loss from the wire and connectors of the spectrum analyzer is about 6dB, so
the total loss is 8dB. We need to deduct this amount from IIP3 calculation. The post-
layout simulation results are shown in Fig 5.20 to compare with the experimental results.
Table 5.6 IIP3 testing results
Pin(dBm) -10 -8 -6 -4 -2 0 IIP3(dBm) Gain(dB)
1st -36 -33.7 -31.8 -30 -28.3 -26.7 8 -18
3rd -72 -66 -60.1 -54.8 -49.2 -44.8
Pin(dBm) -24 -22 -18 -16 -14 -12 IIP3(dBm) Gain(dB)
1st -18.7 -16.89 -14.9 -13 -11.2 -9.5 -12.5 14
3rd -41.77 -35.85 -29.9 -24.1 -19.4 -14.9
Experimental results: IIP3
8
4.5
3
-2
-4.5
-5
-11.5
-12
-13.5
-15
-10
-5
0
5
10
-22 -18 -14 -10 -6 -2 2 6 10 14 18
Gain levels (dB)
IIP
3
(dB
m
)
Fig 5.20 Testing results of IIP3 vs. gain levels
88
Post-layout simulation results: IIP3
9.25
5.9
-1
-3
-10.85
-11.5
-13.6
-15
-10
-5
0
5
10
15
-26 -20 -14 -8 -2 4 10 16 22
Gain levels (dB)
IIP
3
(dB
m
)
Fig 5.21 Post-layout results of IIP3 vs. gain levels
For the VGA gain range from -18 to 14dB, the IIP3 is from 8 to -13.5dBm, as
illustrated in Fig 5.21. Comparing Figs 5.20 and 5.21, the experimental results show that
there are about 1 ~ 2dBm loss in IIP3 from its post-layout simulation results. Overall, for
all gain steps, their IIP3s are all above -14dBm, which is enough for the system
requirement of IIP3 > -15dBm for all gain steps.
V.4.3 Noise characterization
Low noise is an important concern if the input signal is very small and the
bandwidth of interest is very wide. Since we are interested in a very high frequency (up
to 250MHz), the contribution from the 1/f noise at a lower frequency can be neglected.
In this measurement, the spectrum analyzer collects the noise power within the
Resolution Bandwidth (RBW). The noise power per Hz at the output, 2nov , is obtained by
89
dividing the noise power on the spectrum analyzer,
2
,spectrumnv , by the RBW; hence the
noise power per Hz is
RBW
v
v
spectrumn
no
2
,2
= (5.11)
In a further step, the Noise Figure can be calculated in equation 5.8 as
demonstrated in previously,
⋅
+⋅=
BWkTR
INNF
s4
1log10
2
(5.8)
where IN is short for Integrated Input Referred Noise Voltage
Given that in the measurement, RBW = 1MHz, and with equation 5.11, it yields
2
2
,
2
2
2
)0(
250
1
)0( v
spectrumn
v
no
A
MHz
MHz
v
A
BWvIN
×
=
×
= (5.12)
Also, it can be also found that, with Rs = 50, BW = 250MHz, 4kTRs×BW =
1.96 ×10-10 V2. Substitute this result into equation 5.12 yields
( )
××
×
+⋅=
−102
2
,
1096.10
2501log10
v
spectrumn
A
vNF (5.13)
With equation 5.12, the Noise Figure for each gain stage based on the noise
power output measurement result from the spectrum analyzer can be obtained. The
measured output noise power from the spectrum analyzer of the maximum and minimum
gain steps are shown in Figs 5.22 and 5.23.
90
Fig 5.22 Av(0) = 14dB, equivalent output noise level = -79.6dBm, NF = 14.8dB
Fig 5.23 Av(0) = -18dB, equivalent output noise level = -106dBm, NF = 20.53dB
With the output noise power for different gain stages measured, using equation
5.13, the Noise Figure for different gain settings can be calculated. A comparison of
91
Noise Figure results from the measurement with those from the post-layout simulation is
shown in Fig 5.24.
NF with different gain settings
14.8
15.315.6
16.1
17.1
18.0
19.1
19.7
20.5
13.814
14.3
14.6
15.3
16.5
17
17.8
18.8
12.0
14.0
16.0
18.0
20.0
22.0
-22 -18 -14 -10 -6 -2 2 6 10 14 18
Gain levels (dB)
NF
(d
B
)
Experimental
Post-layout
Fig 5.24 Noise Figure (NF): experimental result vs. post-layout
simulation results
As seen in Fig 5.24, the Noise Figure varies from 14.8dB to 20.5dB for all gain
settings, and they all fall in the required range of the system design specifications, which
is less than 25dB for all gain cases. Because the noise performance is a more important
concern in the very small input signal cases as mentioned before, the noise figure at the
maximum gain setting—14dB—should be guaranteed to be lower than the requirement.
The testing results show that the noise figure at the maximum gain is much below the
requirement of NF < 25dB. For the lower gain cases, even though the noise figure is
degraded, and the VGA introduces more noise into the signal it processing, the input
92
signal levels are relatively higher and are more immune to the noise than the very small
signal level at the high gain cases. So, from the system design point of view, as long as
they are all below the required noise level, the degradation of noise performance in the
lower gain cases is still tolerable,.
Comparing the experimental results with post-layout simulation results, the
experimental results deviate from the simulation by about 1 ~ 2dB, which again indicates
the IBM 6HP design-kit has a relatively accurate model on the noise performance of the
circuit.
V.5 Summary of results and comparison
As mentioned, comparing the Figure of Merit (FOM) of all the references with
this work is a more fair approach to compare the overall performance of these VGAs
because it includes the maximum gain range, -3dB bandwidth, signal-to-noise-ratio
(SNR) and the power consumption performance altogether.
AreaPower
TechnologySNR)0( 3,
×
×××
=
− dBMAXV fAFOM (5.10)
Notice that the commonly used units for each specification are different from the
International Standard Unit, for example, AV,MAX(0)’s unit is dB. So, when calculating
the FOM, all the specifications are converted into the International Standard Unit.
Finally, as the FOM will be a very large number if it is still in the International Standard
Unit, it can be expressed in dB instead. Table 5.7 and Figure 5.25 illustrate the results.
93
Table 5.7 Figure of Merit (FOM) comparison
AV,MAX(0)
(dB)
f-3dB
(MHz)
SNR
(dB)
Power
(mW)
Technology Area
(mm2)
FOM
(dB)
[4] 40 495 12.65 54 0.35µm
CMOS
0.15 259
[8] 11 380 35 64 0.25 µm
CMOS
2 223
[9] 34 2000 35 40 0.18 µm
CMOS
0.7 271
This
work
42 425 30 9.5 0.25 µm
CMOS
0.015 310
Figure of Merit (FOM)
0
50
100
150
200
250
300
350
[2] [8] [9] This work
FO
M
(dB
)
FOM (dB)
Fig 5.25 Figure of Merit (FOM) comparison
94
Fig 5.25 shows that this work has the highest Figure of Merit, mainly due to the
highest maximum gain, largest bandwidth, and lowest power consumption among the
VGAs in that comparison.
In summary, from the experimental results and comparing with the state-of-the-
art VGA designs in the literature, the proposed VGA posses: (1) Comparable gain
variable range and the smallest gain steps; (2) Comparable bandwidth with other
designs; (3) Occupies the smallest area; (4) Has the best power consumption among all
designs; (5) Comparable or better than other designs in linearity and noise performance.
95
CHAPTER VI
CONCLUSION
A fully differential CMOS Variable Gain Amplifier (VGA) consisting of
complementary differential pairs with source degeneration, current gain stage with
programmable current mirror, and resistor loads is designed for high frequency and low
power communication applications, such as UWB receiver system. The gain can be
programmed from 0 to 42dB of 2dB/step with -3dB bandwidth greater than 425MHz for
all range of gain. The Third-Order Input Intercept Point (IIP3) is above -7dBm for 1Vpp
differential input and output voltages. These low distortion broadband features are
benefited from the large linear range of the differential pair with source degeneration and
the low impedance internal nodes in the current gain stages. In addition, common-mode
feedback is not required because of these low impedance nodes. Due to the power
efficient complementary differential pairs as input stage, the power consumption is
minimized (9.5mW) for all gain steps. The gain-control scheme includes of fine tuning
(2dB/step) by changing the bias voltage of the proposed programmable current mirror,
and coarse tuning (14dB/step) by switching on/off the source degeneration resistors in
the differential pairs. Capacitive frequency compensation scheme is used to further
extend the VGA bandwidth.
96
The VGA has been designed in the IBM 6HP 0.25µm CMOS processes.
Experimental results demonstrated closed results as the post-layout simulation as
expected.
This VGA topology, benefiting from its features such as ultra-low power
consumption, small die area, large gain range and bandwidth, low distortions, can be
broadly adopted into other immerging communication systems as well.
97
REFERENCES
[1] R. Gomez and A. A. Abidi, “A 50 MHz CMOS Variable Gain Amplifier for
magnetic Data Storage Systems,” IEEE Journal of Solid-State Circuits, vol.35, no.6,
pp.935-939, Jun. 1992.
[2] R. Gomez and A. A. Abidi, “A 50 MHz Variable Gain Amplifier Cell in 2µm
CMOS,” in Proc. IEEE Custom IC Conference, May 1991, pp.9.4.1-9.4.4.
[3] T.-W. Pan and A. A. Abidi, “A 50dB Variable Gain Amplifier Using Parasitic
Bipolar Transistors in CMOS,” IEEE Journal of Solid-State Circuits, vol.24, no.4,
pp.951-961, Aug. 1989.
[4] S.T Tan, and J. Silva-Martinez, “A 270 MHz, 1Vpk-pk, Low-Distortion Variable
Gain Amplifier in 0.35µm CMOS Process,” Analog Integrated Circuits and Signal
Processing, vol.38, no.2, pp.307-310, Feb.2004.
[5] Y. Zheng, J. Yan, and Y. Xu, “A CMOS dB-Linear VGA with Pre-Distortion
Compensation for Wireless Communication Applications,” in Proc. International
Symposium on Circuits and Systems, May 2004, vol.1, pp.813-816.
[6] A. Thanachayanont and P. Naktongkul, “Low-Voltage Wideband Compact CMOS
Variable Gain Amplifier,” Electronics Letters, vol. 41, no. 2, pp.51-52, Jan. 2005.
[7] J. Silva-Martinez, J. Adut, J. M. Rocha-Perez, M. Robinson and S. Rokhsaz, “A
60mW 200 MHz Continuous-Time Seventh-Order Linear Phase Filter with On-Chip
98
Automatic Tuning System,” IEEE Journal of Solid-State Circuits, vol. 38, no.2,
pp.216-225, Feb. 2003.
[8] O. Watanabe, S. Otaka, M.Ashida, and T. Itakura, “A 380MHz CMOS Linear-in-dB
Signal-Summing Variable Gain Amplifier with Gain Compensation Techniques for
CDMA Systems,” in VLSI Circuits Digest of Technical Papers, Jun. 2002, pp.136-
139.
[9] C.-H. Wu, C.-S. Liu and S.-L. Liu, “A 2 GHz CMOS Variable Gain Amplifier with
50dB Linear-in-Magnitude Controlled Gain Range for 10GBase-LX4 Ethernet,” in
IEEE International Solid-State Circuits Conference, vol. 1, Feb. 2004, pp.584-541.
99
APPENDIX A
DETERMINE THE DIMENSIONS FOR THE PROGRAMMABLE
CURRENT MIRROR
In this appendix, it will be shown how equation (3.12) is obtained.
Let us make some assumptions and observations (as shown in Fig 3.4.)
(1) Assume, M1 and M2 have identical dimensions while that of M3 is )/(MLW
(2) Make an equivalent transistor for all the transistors turned on in the bias control
circuit, call it Mb with dimension )/(NLW .
(3) Assume that the bias current for the bias control circuit is correlated to that of the
programmable current mirror. Set Ibias for the current mirror, then Iref = K× Ibias in the
bias control circuit, where K is a constant current gain factor.
Fig A.1 Bias Transistors to generate seven gain steps for programmable current mirror
100
First, notice that 231231 then DSATDSDSATGSDSGS VVVVVV =+=+ , where VDSAT =
VGS – Vth. Since M1 and Mb operate in the saturation region while M3 operates in the
triode region, their drain-source currents are given by
[ ]
[ ])(1
2
1
2
)(1
2
1
2
2
3
333
11
2
11
DSATbDSbDSATbOXnref
DS
DSDSATOXnD
DSATDSDSATOXnD
VVV
NL
WCI
VVV
ML
WCI
VVV
L
WCI
−+=
−=
−+=
λµ
µ
λµ
(A.1)
From Fig 3.9,
1111 ththGSDSDSATDS VVVVVV =+−=− ( ) [ ] 12
1
2
321 thDSDSATOXnD VVVL
WCI λµ +−=∴ (A.2)
[ ] 1
2
1 2
33 thDSATOXnrefDSATbDSAT VVNL
WCIVV λµ +=∴= (A.3)
31 ** DDref IKIKI == (A.4)
Combining equation A3.1, A3.3, and A3.4, we obtain
))/(1(
0 2
2
1
2
33
2
333
2
3
2
3
2
3
33
N
KMNVV
V
NK
MVVVV
N
V
VV
M
K
DSATDS
DSATDSDSATDSDSAT
DS
DSDSAT
−
−=
=+−=
−
(A.5)
Combining equation A3.2, A3.3, and A3.4, we obtain
( ) 33223232 11 DSATDSDSATDSATDSDSAT VNKVVVNVVK =−=− (A.6)
Substituting equation A3.5 into A3.6, we have
))/(11(32 N
KMN
KN
VV DSATDSAT
−
−+= (A.7)
101
The low frequency current gain of programmable current mirror is given by
( )232
2
2
DSDSAT
DSAT
in
out
VV
V
i
i
−
=
(A.8)
Substituting equation A3.6 and A3.7 into A3.8, yields
( )21 MNKNK
i
i
in
out
−−+= (3.12)
Where
( )
( )
( )
( ) bias
ref
b I
I
K
LW
LWN
LW
LW
M === ,
/
/
,
/
/ 1
3
1
Therefore, the low frequency current gain of the programmable current mirror is
a function of the aspect ratios of M1, M3 and Mb, and the ratio between Iref and Ibias. In
the approach used in this design, ( ) ( ) biasref IILWLW /,/,/ 31 are all fixed. By
varying ( )bLW / , different current gains can be obtained.
102
APPENDIX B
THE DIMENSIONS AND CURRENT BIAS FOR THE VGA
1) Calculation of the load resistance
As -3dB frequency (f
-3dB)>350MHz, to leave some margin, choose f-3dB =
400MHz. From this, we can estimate the output resistance we need.
( )outoutdB CRf /13 =− . As we use current mirror connecting to the output resistor, their
parasitic capacitor determines Cout, which would be quite small. Assuming the maximum
parasitic is 0.2pF, and then we can find Rout as
Ω=××××= − KRout 99.1)102.01042/(1 128pi , so choose Rout =1 .5K.
2) Calculation of the source degeneration resistance
Because we need 14dB between adjacent coarse tuning steps, which corresponds
to 5 times of amplification, we can calculate the maximum transconductance of input
stage as
mGdBKG mm 8.16 126425.15 max,max, ===××
Then connect the source degeneration resistor to get a 14dB lower gain than the
maximum gain. From equation 4.5
103
Ω=Ω=
Ω=Ω=
Ω≈Ω≈
==
+
==
+
+
=
450 ,300
9002 ,6002
900 ,600
and // Also
5.01
4.1
5
8.16
5.01
)/1(
22
22
spsn
spsn
spsn
mpspmnsnpnmpmn
mnsn
mn
mnsn
npmn
m
RR
RR
RR
gRgRgg
gR
gm
gR
g
G
µµ
µµ
(B.1)
Finally for the last coarse tuning steps, another 14dB gain reduction is needed.
,5.4 ,3
4.52 ,6.32
4.5 ,6.3
and // Also
5.01
4.1
55
8.16
5.01
)/1(
11
1212
Ω=Ω=
Ω=+Ω=+
Ω≈Ω≈
==
+
=
×
=
+
+
=
KRKR
KRRKRR
KRKR
gRgRgg
gR
gm
gR
g
G
spsn
spspsnsn
spsn
mpspmnsnpnmpmn
mnsn
mn
mnsn
npmn
m
µµ
µµ
(B.2)
3) Calculation of the dimensions and bias current of the input stage
Because we adapt Approach II as mentioned previously to choose the same
dimensions for both differential pairs, the overall transconductance is given by
( )
n
mn
n
npmn
m N
g
N
g
G
+
=
+
+
=
1
4.1
1
/1 µµ
(B.3)
For the maximum gain setting, equation Gm reduces into
mgmggG mnmn
n
p
mnm 12 8.164.11 ===
+=
µ
µ
To further calculate the dimension and bias current of the input stage, we have to
determine VDSAT, Mn, VDSAT, Mp. And this has to meet three different cases VDSAT
requirements, a) high gain range (28 ~ 42dB), b) middle gain range (14 ~ 26dB), and c)
low gain range (0 ~ 12dB).
104
a) 28 ~ 42dB
To accommodate the 1Vpp differential output signal requirement, with 28dB gain,
it corresponds to a 39.9mVpp input signal. So in this case, we have to make VDSAT >40mV.
b) 14 ~ 26dB
With 14dB gain, 1Vpp differential output signal corresponds to a 200mVpp input
signal. As the source degeneration resistor is included, which relaxes VDSAT by (1+N)
times, N = 4, so the VDSAT requirement will be 200mVpp/(1+4) = 40mV.
c) 0 ~ 12dB
With 0dB gain, the required output signal corresponds to a 1Vpp input signal.
With source degeneration, N = 24 in this case, so the VDSAT requirement will be
1Vpp/(1+24) = 40mV
Overall, from the above three cases, with some margin, we set VDSAT,Mn= 150mV
uAImVVmVIg biasMnDSATMnDSATbiasmn 400150 ,12/2 ,, ====
( ) 2
,
/232 gy, technoloIBM6HPfor ,/ because Also VuACVLWCg OXnMnDSATnOXnmn ≈= µµ
( ) ( )
umWW
umLLWLW
pn
pn
78
24.0 ,345//
==
===
4) Calculation of the Dimensions of the Programmable Current Mirror
Because the VGA is needed to handle a 1Vpp differential output signal, the
single-ended signal at the output will be 0.5Vpp. With 1.5K load resistor, the AC current
105
at output will be 0.5/1500 = 0.33mA. As a rule of thumb, to accommodate this AC
current, we must have 3 times larger DC current, which is 1mA. With maximum current
gain of 5, the single ended DC current at the input of the current mirror will be 1mA/5
=0.2mA. Choose 220µA to leave some margin.
For the VDSAT of the current mirrors, choose VDSAT = 150mV to prevent linearity
degradation from the current mirror stage. Now we can calculate the dimensions of the
current mirrors
( )
( ) ( )
umWW
umLLWLW
VuAC
VLWCI
mVVuAI
pn
pn
OXn
MnDSATnOXnbias
DSATbias
24
24.0 ,100//
/232 ,Technology 0.25um 6HPIBMfor
/
2
1
150 ,220
2
2
,
==
===
≈
=
==
µ
µ
The dimensions of the programmable current mirror are given in Table B.1.
106
Table B.1 Dimension of the bias circuits
N 1.01 1.05 1.2 1.4 1.8 3 5.6
Current
Gain (dB)
14 12 10 8 6 4 2
Wb
(W1=24µm)
23.6 21.6 16.8 12 7.2 2.4 0.72
Mb1 Mb2 Mb3 Mb4 Mb5 Mb6 Mb7
W 2 µm 4.8 µm 4.8
µm
4.8
µm
4.8
µm
1.68 µm 0.72 µm
L 0.24 µm
At the end, we can roughly calculate the power consumption of this VGA.
107
VITA
Lin Chen
Texas Instruments,
MS 8749
12500 TI Blvd,
Dallas, Texas 75243
Education
M.E. in Mechanical Engineering, Cornell University, Ithaca, New York, May 2001
B.E. in Automotive Engineering, Tsinghua University, Beijing, China, July 2000
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