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CHARGE PUMP NMOS LDO USING SPLIT-TRANSISTOR
COMPENSATION
BY
Z M Saifullah, B.Sc
A dissertation submitted to the Graduate School
in partial fulfillment of the requirements
for the degree
Master of Sciences, Engineering
Specialization in: Electrical Engineering
New Mexico State University
Las Cruces, New Mexico
March 2015
“CHARGE PUMP NMOS LDO USING SPLIT-TRANSISTOR COMPENSA-
TION,” a dissertation prepared by Z M Saifullah in partial fulfillment of the
requirements for the degree, Master of Sciences has been approved and accepted
by the following:
Dr. Loui ReyesDean of the Graduate School
Chair of the Examining Committee
Date
Committee in charge:
Dr. Paul M. Furth, Associate Professor, Chair.
Dr. Wei Tang, Assistant Professor.
Dr. Abbas Ghassemi, Professor.
ii
DEDICATION
Dedicated to my mother Tahmin Ara Begum, father Md. Liakat Ali, wife
Kamrun Nahar, daughter Jemima Saifullah, sister Nusrat Zunaid and her family,
And my grand parents
iii
ACKNOWLEDGMENTS
I would like to thank my parents Tahmin Ara Begum and Md. Liakat
Ali for their support and their decision to let me have my Master’s in USA. My
wife Kamrun Nahar who supported me in my endeavor. Without her love and
encouragement, i could not have completed my degree. My daughter Jemima
Saifullah who gave me new meanings of life. And my sister Nusrat Zunaid, her
husband Muhammed Zunaid, their children Navid Zunaid and Nuzhat Zunaid who
encouraged me to complete my Master’s in USA.
I would like to thank Dr. Paul M. Furth for advising me throughout my
Master’s degree. I learned a great deal from his teaching through courses like
digital VLSI and Integrated Power Management; learned how to do research and
research philosophy through his research. His kind and supportive behaviour
encouraged me to do a competitive research. I thank his wife, Carol and family
with whom we spent time on Thanksgiving day every year. They made me feel
like home when i am thousands miles away from it.
Great appreciation and thanks to Dr. Wei Tang and Dr. Abbas Ghassemi
for accepting my request to be member of my thesis committee , managing time
from their busy schedule.
I would also like to thank Dr. Jaime Ramirez for developing my analog
VLSI concept.
iv
I would like to thank my friends, Muhammed Junayet Hossain, Md. Atiqul
Haque, Md. Adnan Sarker, Alejandro Romn Loera, Sri Harsh Pakala, Bala Ke-
sava, Yeshwanth Puppala, Venkat Harish Nammi, Anurag Veerabathini. They
inspired and helped me whenever needed.
v
VITA
April 7, 1984 Born in Bangladesh.
Education
2002- 2006 B.Sc. in Electrical and Electronic Engineering,Khulna University of Engineering and Technology, Bangladesh
2012 - 2015 MSEE. in Electrical Engineering,New Mexico State University, USA - GPA 3.88/4.0
Experience
Teaching Assistant, Electrical Engineering, NMSU, Fall-2013, Spring 2014
vi
ABSTRACT
CHARGE PUMP NMOS LDO USING SPLIT-TRANSISTOR
COMPENSATION
BY
Z M Saifullah, B.Sc
Master of Sciences, Engineering
Specialization in Electrical Engineering
New Mexico State University
Las Cruces, New Mexico, 2015
Dr. Paul M. Furth, Chair
Two NMOS Low-Dropout Voltage Regulators (LDO) are designed in IBM
180 nm CMOS process for an output of 1.2 VDC with load current that can vary
from 3 µA to 100 mA. Dropout voltages for the LDOs are 177 mV and 82 mV at
maximum load current. There is no resistors divider in the designs as the output
voltage and reference voltage is the same. A charge pump circuit is implemented
in the IC to increase the gate voltage of the NMOS pass transistor so that the
dropout is low. Charge pump is so designed that when there is no reference
voltage, the charge pump will not work, making the LDOs more efficient. A two-
phase non-overlapping clock generator is used to avoid the charge sharing of the
capacitors in the charge pump. A clock input is required in the clock generator to
vii
have non-overlapping two-phase outputs. Split-length transistor with varied width
is implemented in these designs. Both circuits have low quiescent current of 3.5 µA
without charge pump and non-overlapping clock generator. With charge pump
and non-overlapping clock generator circuits the quiescent current still below 4 µA.
LDOs are also tested for line transisent, load transient, PSR and ripple. Ripple
is caused by the input clock to the clock generator. When there is no clock, the
ripple goes away. All tests are performed in hardware and simulation, and results
are compared with each other.
viii
TABLE OF CONTENTS
LIST OF TABLES xiii
LIST OF FIGURES xv
1 INTRODUCTION 1
1.1 Power Management of Cell Phone Architecture . . . . . . . . . . . 1
1.2 Motivation . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 2
1.3 Specifications . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 3
1.4 Unique Contributions . . . . . . . . . . . . . . . . . . . . . . . . . 3
1.5 Organization of This Thesis . . . . . . . . . . . . . . . . . . . . . 3
2 LITERATURE REVIEW 5
2.1 Basics of LDOs . . . . . . . . . . . . . . . . . . . . . . . . . . . . 5
2.2 Conventional Design of PMOS LDO . . . . . . . . . . . . . . . . . 6
2.3 Conventional Design of NMOS LDO . . . . . . . . . . . . . . . . 8
2.4 Performance Parameters of LDOs . . . . . . . . . . . . . . . . . . 10
2.4.1 Dropout Voltage . . . . . . . . . . . . . . . . . . . . . . . 10
2.4.2 Line Transient and Line Regulation . . . . . . . . . . . . . 11
2.4.3 Load Transient and Load Regulation . . . . . . . . . . . . 12
2.4.4 Power Supply Rejection . . . . . . . . . . . . . . . . . . . 13
2.4.5 Recovery Time . . . . . . . . . . . . . . . . . . . . . . . . 14
ix
2.4.6 Gain Margin and Phase Margin . . . . . . . . . . . . . . . 15
2.5 Compensation Techniques . . . . . . . . . . . . . . . . . . . . . . 16
2.5.1 Miller Compensation . . . . . . . . . . . . . . . . . . . . . 17
2.5.2 Nested Miller Compensation . . . . . . . . . . . . . . . . . 18
2.5.3 Reverse-Nested Miller Compensation with Nulling Resistor 20
2.6 Split-Length Transistors . . . . . . . . . . . . . . . . . . . . . . . 21
2.7 Split-Length Compensation . . . . . . . . . . . . . . . . . . . . . 22
2.8 Non-Overlapping Clock Generator Circuit . . . . . . . . . . . . . 24
3 DESIGN AND SIMULATIONS 27
3.1 Proposed Low-Dropout Voltage Regulators . . . . . . . . . . . . . 27
3.2 Proposed LDO Regulator Architecture and Design . . . . . . . . . 28
3.3 Small Signal Analysis . . . . . . . . . . . . . . . . . . . . . . . . . 31
3.3.1 First Stage . . . . . . . . . . . . . . . . . . . . . . . . . . . 31
3.3.2 Second Stage . . . . . . . . . . . . . . . . . . . . . . . . . 34
3.3.3 Gain in Level Shifter . . . . . . . . . . . . . . . . . . . . . 34
3.3.4 Output Stage . . . . . . . . . . . . . . . . . . . . . . . . . 35
3.3.5 Charge Pump Operation . . . . . . . . . . . . . . . . . . . 36
3.3.6 Non-overlapping Clock Genarator Design . . . . . . . . . . 38
3.3.7 Poles and Zeros . . . . . . . . . . . . . . . . . . . . . . . . 40
3.4 Simulation Results . . . . . . . . . . . . . . . . . . . . . . . . . . 41
3.4.1 AC Analysis . . . . . . . . . . . . . . . . . . . . . . . . . . 41
3.4.2 Dropout Voltage Measurement . . . . . . . . . . . . . . . . 43
3.4.3 Line Transient . . . . . . . . . . . . . . . . . . . . . . . . . 47
3.4.4 Load Transient . . . . . . . . . . . . . . . . . . . . . . . . 51
3.4.5 Ripple . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 55
x
3.4.6 Power Supply Rejection . . . . . . . . . . . . . . . . . . . 56
4 EXPERIMENTAL RESULTS 61
4.1 Layout . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 61
4.1.1 Passive Elements Layout . . . . . . . . . . . . . . . . . . . 61
4.1.2 Pass Element Layout . . . . . . . . . . . . . . . . . . . . . 62
4.1.3 Layout of Other Circuits . . . . . . . . . . . . . . . . . . . 63
4.2 Hardware Results . . . . . . . . . . . . . . . . . . . . . . . . . . . 66
4.2.1 Dropout Voltage . . . . . . . . . . . . . . . . . . . . . . . 67
4.2.2 Ripple Measurement . . . . . . . . . . . . . . . . . . . . . 68
4.2.3 Line Transient Response . . . . . . . . . . . . . . . . . . . 69
4.2.4 Load Transient Response . . . . . . . . . . . . . . . . . . . 76
4.2.5 PSR Measurements . . . . . . . . . . . . . . . . . . . . . . 76
5 DISCUSSION AND CONCLUSION 81
5.1 Result Comparison : Simulated vs. Measured . . . . . . . . . . . 81
5.2 Comparison with Existing Designs . . . . . . . . . . . . . . . . . . 85
5.3 Future Work . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 87
APPENDICES 91
A. Test Document 92
A.1 With PCB: . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 93
A.1.1 Procedure to Measure Dropout Voltage VDO . . . . . . . . 93
A.1.2 Line Transient Test Procedure . . . . . . . . . . . . . . . . 94
A.1.3 Load Transient Test Procedure . . . . . . . . . . . . . . . 97
A.2 With Bread Board . . . . . . . . . . . . . . . . . . . . . . . . . . 97
xi
B. Maple 98
REFERENCES 100
xii
LIST OF TABLES
3.1 Device dimensions in µm for the LDO1 and LDO2. . . . . . . . . 29
3.2 Component’s values used in both LDOs. . . . . . . . . . . . . . . 29
3.3 Device dimensions in µm for Charge Pump. . . . . . . . . . . . . 38
3.4 Device dimensions in µm for Non-overlapping Clock Generator. . 40
3.5 AC analysis for LDO1 and LDO2 Regulator at IL,min = 3µA andIL,max = 100 mA. . . . . . . . . . . . . . . . . . . . . . . . . . . 42
3.6 Simulated dropout voltage for LDO1 and LDO2 at maximum loadwith and without the charge pump and the capacitor CBATT . . . 46
3.7 Line transient simulation results for LDO1 and LDO2 regulators. 47
3.8 Load transient simulation results for LDO1 and LDO2 regulator. 52
4.1 Layout Area for LDO1 and LDO2 regulators and Components. . . 63
4.2 Experimental dropout voltage for LDO1 and LDO2 at maximumload. . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 68
4.3 Line transient experimental results for proposed LDOs. . . . . . 71
4.4 Load transient experimental result for proposed LDOs. . . . . . . 77
5.1 Results Comparison for LDO1. . . . . . . . . . . . . . . . . . . . 83
5.2 Results Comparison for LDO2. . . . . . . . . . . . . . . . . . . . 84
5.3 Simulated dropout voltage for LDO1 and LDO2 at maximum load. 84
5.4 Comparison table with existing NMOS LDO. . . . . . . . . . . . . 88
5.5 Comparison table with existing PMOS LDO. . . . . . . . . . . . . 89
xiii
1 Dropout Voltage Measurement Table . . . . . . . . . . . . . . . . 95
xiv
LIST OF FIGURES
1.1 Block diagram of typical cell phone architecture [1]. . . . . . . . 2
2.1 Block diagram of low drop-out (LDO) regulator. . . . . . . . . . . 6
2.2 Block diagram of PMOS low drop-out (LDO) regulator. . . . . . . 7
2.3 Block diagram of NMOS low drop-out (LDO) regulator. . . . . . . 9
2.4 Typical Dropout Voltage Measuring Waveform. . . . . . . . . . . 10
2.5 Typical Line Transient Waveform. . . . . . . . . . . . . . . . . . . 11
2.6 Typical Load Transient Waveform. . . . . . . . . . . . . . . . . . 13
2.7 Waveforms showing typical PSR response [7] . . . . . . . . . . . 14
2.8 Waveforms describing recovery times in case of a line transient event 15
2.9 Illustration on measuring gain margin and phase margin [9] . . . 16
2.10 Two-stage miller compensated op-amp with nulling resistor . . . 17
2.11 Simplified AC characteristic for Miller Compensation without NullingResistor [12] . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 19
2.12 Simplified AC characteristic for Miller Compensation with NullingResistor [12] . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 19
2.13 Nested Miller compensation. . . . . . . . . . . . . . . . . . . . . . 20
2.14 Reverse-nested Miller compensation. . . . . . . . . . . . . . . . . 21
2.15 Illustration of split-length transistors. . . . . . . . . . . . . . . . . 22
2.16 Illustration of split-length compensation for NMOS. . . . . . . . . 23
2.17 Small signal model for split-length compensation for NMOS. . . . 23
xv
2.18 Schematic of a typical Non-overlapping clock generator [17]. . . . 25
2.19 Output waveforms phase 1 and phase 2 of the non-overlapping clockgenerator [17]. . . . . . . . . . . . . . . . . . . . . . . . . . . . . 26
3.1 Schematic for the proposed LDO. . . . . . . . . . . . . . . . . . . 28
3.2 Schematic of the Proposed LDO1 with Compensation Capacitor. . 30
3.3 Schematic of the Proposed LDO2 with Compensation Capacitor. . 31
3.4 Small-signal architecture of LDO1. . . . . . . . . . . . . . . . . . 32
3.5 Small-signal architecture of LDO2. . . . . . . . . . . . . . . . . . 33
3.6 Schematic of the designed Charge Pump. . . . . . . . . . . . . . . 38
3.7 Charge Pump operation. . . . . . . . . . . . . . . . . . . . . . . . 39
3.8 Schematic of the designed non-overlapping clock generator, whichuses 7 delay cells in each path. . . . . . . . . . . . . . . . . . . . . 41
3.9 Testbench for AC analysis. . . . . . . . . . . . . . . . . . . . . . . 43
3.10 LDO1 AC analysis. . . . . . . . . . . . . . . . . . . . . . . . . . . 44
3.11 LDO2 AC analysis. . . . . . . . . . . . . . . . . . . . . . . . . . . 45
3.12 Test bench for dropout voltage simulation. . . . . . . . . . . . . . 46
3.13 Test bench for line transient simulation. . . . . . . . . . . . . . . 48
3.14 Line Transient Response for LDO1. . . . . . . . . . . . . . . . . . 49
3.15 Line Transient Response for LDO2. . . . . . . . . . . . . . . . . . 50
3.16 Testbench for load transient simulation. . . . . . . . . . . . . . . . 52
3.17 LDO1 load transient response. . . . . . . . . . . . . . . . . . . . . 53
3.18 LDO2 load transient response. . . . . . . . . . . . . . . . . . . . . 54
3.19 Test Bench for Ripple measurement. . . . . . . . . . . . . . . . . 55
3.20 Ripple measurement for LDO1 at Load Current = 1 mA. . . . . . 56
3.21 Ripple measurement for LDO2 at Load Current = 1 mA.. . . . . . 57
3.22 Test Bench for PSR measurement. . . . . . . . . . . . . . . . . . . 58
xvi
3.23 PSR waveform for LDO1. . . . . . . . . . . . . . . . . . . . . . . 59
3.24 PSR waveform for LDO2. . . . . . . . . . . . . . . . . . . . . . . 60
4.1 Microscopic view of LDO1 (Die measure 1.5 mm x 1.5 mm). . . . 62
4.2 Layout of LDO1 (Dimension 275 µm x 437 µm). . . . . . . . . . . 64
4.3 Layout of LDO2 (Dimension 424 µm x 437 µm). . . . . . . . . . . 65
4.4 Layout of LDO1 with 40-pin pad frame (1.5 mm x 1.5 mm). . . . 66
4.5 Layout of 10 pF Capacitor. . . . . . . . . . . . . . . . . . . . . . . 67
4.6 Layout of 200 kΩ resistor. . . . . . . . . . . . . . . . . . . . . . . 68
4.7 Layout of NMOS Pass Element (Dimensions 44.65 µm x 127.97 µm). 69
4.8 LDO1 Dropout Voltage Measurement. . . . . . . . . . . . . . . . 70
4.9 LDO2 Dropout Voltage Measurement. . . . . . . . . . . . . . . . 71
4.10 Waveform for measuring Ripple for LDO1. . . . . . . . . . . . . . 72
4.11 Waveform for measuring Ripple for LDO2. . . . . . . . . . . . . . 73
4.12 Line Transient Response for LDO1. . . . . . . . . . . . . . . . . . 74
4.13 Line Transient Response for LDO2. . . . . . . . . . . . . . . . . . 75
4.14 Load Transient Response for LDO1. . . . . . . . . . . . . . . . . . 76
4.15 Load Transient Response for LDO2. . . . . . . . . . . . . . . . . . 77
4.16 PSR waveform for LDO1. . . . . . . . . . . . . . . . . . . . . . . 79
4.17 PSR waveform for LDO2. . . . . . . . . . . . . . . . . . . . . . . 80
5.1 Charge Pump operation. . . . . . . . . . . . . . . . . . . . . . . . 85
5.2 Measured and Simulated PSR values for LDO1. . . . . . . . . . . 86
5.3 Measured and Simulated PSR values for LDO2. . . . . . . . . . . 87
A.4 Jumper Configuration for Dropout measurement. . . . . . . . . . 93
xvii
Chapter 1
INTRODUCTION
This is the age of mobility, accessibility and dependability. We are always on the
run and want to gain immediate access to information that we need. And for this,
we are dependent on mobile devices such as the smart phones, tablets, laptops,
etc. All of these portable devices that we use in our day-to-day life can be made
functional only when we have power. And batteries are the only source of power
for these devices, hence a critical component.
1.1 Power Management of Cell Phone Architecture
Fig. 1.1 shows the block diagram of a typical cell phone architecture. The
major functional blocks are the power amplifier, RF section, analog base band and
digital base band units. One or more voltage regulators supply power to all of
those blocks. The supply voltage and current requirements of the different blocks,
which correspond to the output requirements of the regulators, depend on the
phone generation, the technology used and the system design of the phone [1].
Mobile devices impose power savings as much as possible to extend the
time between charging of the battery. This is where linear regulators come in
handy. A linear regulator is a system that can deliver a constant output voltage.
An LDO (Low Dropout Voltage Regulator) is one kind of linear regulator. It is
a device that can produce regulated (constant) output for different load currents.
The reason behind LDOs popularity is because it can produce a low-noise output,
consumes low power, and requires small area. Simplicity in design is an added
1
Figure 1.1: Block diagram of typical cell phone architecture [1].
advantage. Due to their low quiescent current and low noise contribution, LDOs
are preferred to use in some blocks of cellular and portable devices. They are very
suitable for powering the baseband, RF, TCXO, RTC, and audio sections of the
typical handset [2]. LDO’s can also be used to reduce the output ripple of other
converters. Hence LDOs are considered an integral part of power management
systems. Fig. 1.1 shows that LDOs are used to power up digital and analog base
band, display, flash, SRAM, VCOs and power amplifier.
1.2 Motivation
The wide usage and popularity of low drop-out regulators made us inter-
ested to work on them. The PMOS LDO is the most widely-used LDO. Because of
higher ripple cancellation property of NMOS along with higher mobility, we chose
to study the NMOS LDO. We assume NMOS LDO have higher power supply
rejection and require less area in comparison with PMOS LDO. Our goal was to
study an NMOS LDO and compare its performance parameters with other NMOS
and PMOS LDOs in literature.
2
1.3 Specifications
The goal is to generate a regulated output of 1.2 Volts for load currents
varying from 3 µA to 100 mA. The total quiescent current is meant to be less than
5 µA. The work will be done in a 0.18 µm IBM process. The load capacitance is
100 pF. Our goal is to achieve a maximum drop-out voltage of 100 mV. We also
want to keep the clock ripple as low as 0.5% of output voltage.
1.4 Unique Contributions
1. Designed and fabricated an NMOS LDO.
2. Used split-transistor compensation technique.
3. Designed a working charge pump to drive the NMOS pass transistor.
1.5 Organization of This Thesis
The report is organized in the following way. In Chapter 2, we discuss
the basics of both PMOS and NMOS LDOs. Chapter 2 includes the operation of
conventional LDOs. We define some important parameters and also discuss some
basics of compensation techniques.
In Chapter 3, design parameters, simulations and simulation results are
discussed along with the design procedure and criteria. We also include AC anal-
ysis of the designed LDOs in this chapter.
In Chapter 4, the layout is described. It also includes hardware measure-
ment results, PCB design and the test setup for testing different parameters.
Chapter 5 compares the simulated results and the measured results. We
find comments and conclusions regarding our work.
In the appendix, we have a detailed description of test procedures and the
layout of our PCB. The latter part of the appendix includes Maple work which is
used to estimate the poles and zeros of the LDOs. Matlab code to plot simulation
3
and experimental results is also included here. Last but not the least, we find the
list of references that are used to complete our work and can be very influential
for the future work.
4
Chapter 2
LITERATURE REVIEW
DC-DC converters transform one DC level to another DC level. The low dropout
voltage regulator is a type of DC-DC converter that is a buck converter. The LDO
is a linear voltage regulator and is usually used as a low-noise voltage source. In
this chapter, we will discuss the basics of LDOs and their operation. A few
compensation techniques will also be discussed in this chapter.
2.1 Basics of LDOs
An LDO consists of several working blocks including an error amplifier,
pass element and feedback network, as shown in Fig. 2.1. The pass element can
be either a PMOS or NMOS transistor and is usually very large in size so that
it can accommodate high output current. The pass element is a critical part of
the LDO. A PMOS pass element in an LDO is configured as a common-source
amplifier, whereas an NMOS pass element is configured as a source-follower. The
function of the feedback network is to provide a comparable negative feedback
value for the negative input terminal of the error amplifier. A voltage divider is
also a part of the feedback network. A voltage divider network is not necessary
for the LDO if the output voltage is equal to the reference voltage. The positive
input terminal of the error amplifier is always attached to a reference voltage. The
output voltage of the LDO can be expressed as a function of the reference voltage
5
using:
VOUT = VREF ·(
1 +R2
R1
)(2.1)
The function of the amplifier is to compare the two values. For a small
change in the output voltage, through the feedback network, this change appears
at the negative input terminal of the error amplifier. The small difference between
the two input terminals gets amplified by the error amplifier and controls the gate
terminal of the pass element to eventually stabilize the output voltage.
VREF
VBATT
Pass Element
R1
R2
Feedback
Network
Error_Amplifier
VOUT
CL
OA
D
Figure 2.1: Block diagram of low drop-out (LDO) regulator.
2.2 Conventional Design of PMOS LDO
Most of the commercially-available LDOs use PMOS pass elements. Fig. 2.2
shows the block diagram of a typical PMOS LDO. We find from the schematic
that the open loop gain of the LDO is the product of the gain of the error amplifier
and the gain of pass element which is in a common-source configuration. Note
6
that the input terminals are reversed because the PMOS pass element configured
as a common-source amplifier is inverting. The output voltage is fed back to the
positive input terminal of the error amplifier.
VREF
VBATT
MPPASS
R1
R2
Negative
Feedback
Error_Amplifier
VOUT
RL
OA
D
CL
OA
D
G
D
S
Figure 2.2: Block diagram of PMOS low drop-out (LDO) regulator.
Basically, a three-stage LDO forms at least a two-pole transfer function
[3]. One pole is the contribution of the load capacitor and pass element and is
usually the dominant one when there is a large off-chip capacitor. Another one is
from the output of the error amplifier driving the large pass element. In the case
of a two-pole system, we can express the transfer function as:
AOL(s) =AEA.APE
(s+ ωPA).(s+ ωPO)(2.2)
where
AOL(s) is the open-loop gain of the LDO
7
AEA is the gain of the error amplifier
APE is the gain of the pass element
ωPA is the pole at the output of the error amplifier
ωPO is the pole at the output of the pass element
Other poles and zeros may exist inside the error amplifier.
The conditions for a stable two-pole system are that the poles are far apart
and, moreover, the second pole is two or three times the Unity Gain Frequency
(UGF) of the LDO [3]. The UGF is determined by the capacitor that sets the
dominant pole along with the transconductance of the error amplifier that sets the
gain [4]. Noise that may occur in the LDO can primarily be removed by placing a
large capacitor at the output node. We need to design the system in such a way
that we have proper gain margin and phase margin, which will be discussed in
more detail later.
Because of electron mobility is generally two to three times higher than
hole mobility, the effective resistance of an NMOS pass element is two to three
times smaller than a PMOS pass element, which can be calculated using
reffective =1
(WL
)µCox(V gs− V t)(2.3)
So to get the same dropout performance, the NMOS LDO occupies less area
because of the smaller pass element size than a PMOS LDO. Hence for the same
dropout performance, the cost is lower for an NMOS LDO than for a PMOS LDO.
2.3 Conventional Design of NMOS LDO
LDOs not only provide the required voltages, they also provide the neces-
sary current to the circuit. When designing an NMOS LDO, we need to consider
8
that the gate voltage of the NMOS pass element needs to be higher than the
source voltage of the pass element so that it can accommodate high current. As
such, we need to boost the voltage of the system at the gate of the pass element.
In Fig. 2.3 we see a level shifter in series with the gate of the pass element. The
function of the level shifter is to increase the DC voltage that it receives from the
output of the error amplifier. The level shifter could be a battery or a capaci-
tor. If a capacitor is used, an additional high voltage supply or a charge pump is
required.
VREF
VBATT
Level Shifter
MNPASS
R1
R2
Negative
Feedback
Error_Amplifier
VOUT
RL
OA
D
CL
OA
D
G
S
D
Figure 2.3: Block diagram of NMOS low drop-out (LDO) regulator.
All other blocks are the same for both types of LDOs. The NMOS LDO
has an error amplifier which converts the difference between the feedback signal
and the reference signal to an output voltage that is applied to one terminal of
the level shifter. The level shifter then adds the additional DC voltage from an
9
outside source and applies the voltage to the gate of the pass transistor. The pass
transistor then controls the output based on the signal applied at the gate.
2.4 Performance Parameters of LDOs
The performance of an LDO can depend on the needs of the customers or
the circuit where it will be used. The most important parameters that we consider
during our design are discussed in this section.
2.4.1 Dropout Voltage
The dropout voltage VDO can be defined as the input-to-output differential
voltage where the circuit can no longer regulate its output voltage (VOUT ). In our
work, we adopted a more specific definition of the dropout voltage as the difference
between the input and output voltages when the output voltage is 5% below the
regulated output voltage VOUT,MAX . A typical figure that shows the process of
measuring dropout voltage is shown in Fig. 2.4 where rise and fall times are very
slow. Dropout voltage VDO is measured by the formula:
VDO = (VIN − VOUT ) |VOUT=VOUT,MAX−VOUT,MAX∗5% (2.4)
Time (s)
Volt
age
(V)
VIN
VOUTVDO=VIN-VOUT|VOUT,MAX-VOUT,MAX*5%
VOUT,MAX
VDOVOUT,MAX*5%
Figure 2.4: Typical Dropout Voltage Measuring Waveform.
10
2.4.2 Line Transient and Line Regulation
VIN
VOUT
trise tfall
Overshoot
Undershoot
VOUT,SS
VIN
VIN
VOUT
trise tfall
Overshoot
Undershoot
VOUT,SS
VIN
Figure 2.5: Typical Line Transient Waveform.
Fig. 2.5 shows a typical line transient response. The input signal has sharp
rise and fall times, trise and tfall, respectively. When the input signal rises, we
observe a fast rise in the output voltage, which eventually diminishes to a steady-
state value due to the controlling properties of the LDO. This fast rise in the
output is known as overshoot. Similarly, during the falling edge of the input
signal, there is an undershoot in the output waveform. In other words, the output
voltage tends to fall below the specified voltage. Line transient performance is
summarized by
∆VOUT,LINE = Overshoot + Undershoot + ∆VOUT,SS (2.5)
where ∆VOUT,SS is the the difference between the stable output voltages after an
overshoot and an undershoot.
Line regulation can be defined as the ability to maintain a steady-state
output voltage with variation in the supplied input voltage. Line regulation is
11
measured as the ratio of the steady-state change in VOUT (∆VOUT,SS) to the steady-
state change in VIN (∆VIN).
Line Regulation =∆VOUT,SS
∆VIN
(2.6)
Units for expressing line regulation are generally mV/V.
2.4.3 Load Transient and Load Regulation
Like line regulation, load regulation is also a measure of maintaining a
steady output, but this time the variation occurs in the load current. So, load
regulation can be defined as the ability to maintain a steady state output with
the variation in the load current. When there is a sharp rise in the load current,
the output voltage tends to go down, causing undershoot, and then climb back
near to the desired output. Similarly, when the load current goes from high to
low, we can observe a peak in the output voltage which eventually settles down to
the desired output. This peak is known as overshoot. And the voltage where the
output settles is known as the steady state output voltage. Fig. 2.6 shows a sample
output waveform for load transient measurement. Load transient is summarized
using
∆VOUT,LOAD = Overshoot + Undershoot + ∆VOUT,SS (2.7)
Load Regulation is measured as the ratio of the steady-state change in VOUT
(∆VOUT,SS) to the change in IL (∆IL).
Load Regulation =∆VOUT,SS
∆IL(2.8)
The units useful expressing load regulation are typically mV/mA.
12
VOUT
IL
Undershoot
OvershootVOUT,SS
IL
trisetfall
Figure 2.6: Typical Load Transient Waveform.
2.4.4 Power Supply Rejection
Power Supply Rejection (or ripple rejection) is a measure of the AC cou-
pling between the input supply voltage and the output voltage [5]. There are
contradictory statements regarding PSR relating to NMOS and PMOS LDOs. A
PMOS pass element generally has better PSR than an NMOS pass element ac-
cording to [5]. On the other hand, [6] states that an NMOS pass element has
better PSR over a PMOS pass element.
Supply voltage ripple affects analog and RF blocks. An LDO with good
PSR can overcome this problem. Ripple can be introduced into the system from
the reference generator voltage and the error amplifier at low frequencies. At high
frequencies, noise is introduced through the pass element. PSR depends mainly
on the loop gain. The higher the loop gain is, the higher the PSR is. That is
the reason that at low frequency, the LDO has better PSR than it does at high-
frequency. Fig. 2.7 shows a typical response of PSR measurement waveform for
an operational amplifier [7].
13
Figure 2.7: Waveforms showing typical PSR response [7]
2.4.5 Recovery Time
Recovery time is the time taken by the LDO to settle back within a specified
tolerance band of its steady-state output voltage VOUT,SS after an overshoot or
undershoot event [8]. In Fig. 2.8, tRH is the recovery time after an overshoot
event and tRL is defined as the recovery time after an undershoot event, where
the specified tolerance band is 1% of the output voltage. The average recovery
time tR is given by
tR ≡tRH + tRL
2(2.9)
.
14
Figure 2.8: Waveforms describing recovery times in case of a line transient event
2.4.6 Gain Margin and Phase Margin
Phase margin (PM) is defined as the difference between the phase and -
180o at the unity gain frequency. It is usually measured in degrees. The gain
margin (GM) is the amount of gain increase required to make the loop gain unity
at the frequency where the phase angle is -180o. The unit for GM is dB. Fig. 2.9
shows typical measurement techniques for gain margin and phase margin using
an AC analysis.
For a negative feedback network, if the feedback signal has the same mag-
nitude and phase as the input signal, the output signal will be unstable. To make
the system stable, we need to have a gain margin of at least 10 dB and a minimum
required phase margin of 45 degrees. Anything below these values is marginally
stable or unstable [10].
15
Figure 2.9: Illustration on measuring gain margin and phase margin [9]
The higher the phase margin is, the more stable the system is. At a phase
margin of 45 degrees, the output will have some ringing. A phase margin of 60
degrees usually does not show any ringing, hence the recovery time is quicker.
A system with 90 degrees phase margin is more stable, but the recovery time
increases. A 60 degrees phase margin is considered the optimum value.
2.5 Compensation Techniques
The more stages in an amplifier, the more complex its compensation net-
work becomes in order to maintain a stable system. Compensation techniques
depend on the number and types of stages used in the amplifier. Several compen-
sation techniques are discussed in this section.
16
2.5.1 Miller Compensation
-GM1VIN VOUT-GM2
CC RC
ROUTCOUT
V1
R1C1
Figure 2.10: Two-stage miller compensated op-amp with nulling resistor
The Fig. 2.10 shows a two-stage amplifier with Miller compensation. This
is probably the most widely used compensation technique [11]. Capacitor CC
is the compensation capacitor, and resistor RC is the called the nulling resistor.
Miller compensation can also be used without the nulling resistor. Basically, Miller
compensation is a series capacitor and resistance from the output of the second
stage to the output node of the previous stage. At high frequencies it creates
a feed forward path, which may be undesireable. In the figure, GM1 and GM2
are the transconductance of stage one and stage two, respectively. The Miller
capacitance causes the dominant pole at the output of the first stage to move to
a lower frequency. The dominant pole equation is:
ωP1 =1
AV 2 ·R1 · CC
(2.10)
17
And for the non-dominant pole at the output node, it moves towards high
frequencies. The second pole equation is:
ωP2 =GM2 · CC
CC · CL + CC · C1 + C1 · CL
(2.11)
Capacitor CC also creates a right hand zero, which can be expressed with-
out the nulling resistance as:
ωZ =GM2
CC
(2.12)
With the nulling resistance in, the poles remain the same, only the zero
moves from the right half plane to the left half plane as followe:
ωZ1 =1
CC · ( 1RC− gm2)
(2.13)
With a properly chosen value of RC , we can shift the zero to any suitable
position. In fact, the value of ωZ1 can help improve the performance of the
amplifier. Figs. 2.11 and 2.12 show the AC characteristics of an amplifier before
and after adding Miller compensation.
2.5.2 Nested Miller Compensation
Fig. 2.13 shows a graphical depiction of the nested Miller compensation
technique, which is an extension of Miller compensation which we use for multi-
stage amplifier, and only the Miller compensation is not good enough to stabilize
the circuit. Here we can see a capacitor, CC1 is connected from the final output
node to the first stage output node and also another capacitor CC2 is connected
from the same final output node to the output node of the second stage. Most
18
Figure 2.11: Simplified AC characteristic for Miller Compensation without NullingResistor [12]
Figure 2.12: Simplified AC characteristic for Miller Compensation with NullingResistor [12]
interestingly, both capacitors, CC1 and CC2, are generally connected through a
single resistor, RC .
So, can we just connect the output of one stage to the output of another
stage? The answer is NO. We need to keep in mind that the feedback must always
be negative. Now, if we look at the final stage, it is an inverting stage; hence the
feedback through CC2 is negative [13]. Since the second stage is non-inverting but
final stage is inverting, the feedback through CC1 is again negative [13]. Nested
Miller Compensation does not affect the overall gain of the amplifier, but rather
helps to improve the stability by creating two left half plane zeros.
For the configuration shown, the dominant left half pole equation is:
19
+GM2-GM1VIN VOUT-GM3
CC1
CC2
RC
R2C2
ROUTCOUT
V1 V2
R1C1
Figure 2.13: Nested Miller compensation.
ωP1 =1
AV 2 · Aout ·R1 · CC1
(2.14)
where, AV 2 = R2 ·GM2, and Aout = ROut ·GM3, and the dominant left half plane
zero equation is:
ωZ1 =1
−CC2
gM3+RC2 · CC2 +RC1 · CC1
(2.15)
2.5.3 Reverse-Nested Miller Compensation with Nulling Resistor
In Fig. 2.13, nested Miller compensation was possible because the middle
stage was non-inverting and the final stage was inverting. Now, consider a three-
stage amplifier with the stages as non-inverting, inverting and non-inverting, re-
spectively, for stages one to three. How can we compensate this amplifier? Nested
Miller will definitely not work here because of the positive feedback from the fi-
20
-GM1VIN VOUT-GM2 +GM3
CC1
CC2
RC
R2C2 RO
UT
COUT
V1 V2
R1C1
Figure 2.14: Reverse-nested Miller compensation.
nal stage to the output of the second stage. Reverse nested Miller compensation
was introduced to avoid this problem. Here, a capacitor CC1 is connected from
the output stage to the output of stage one and capacitor CC2 is connected from
the output of second stage to the output of the firstl stage. Like nested Miller
compensation, this compensation can also have a common resistor RC known as
a nulling resistor, as shown in Fig. 2.14. Both capacitors have negative feedback
paths. With the proper value of the compensation components, we can generate
two left half plane zeros which can help to create a stable system [14, 15].
2.6 Split-Length Transistors
The Figure 2.15 shows an illustration of split length transistors for both
NMOS and PMOS transistors. This technique was first introduced by Saxena [16].
Though this is not a widely used technique yet, we have designed an LDO keeping
the split length compensation technique in mind. In Fig. 2.15(a) we can see an
NMOS transistor M1 of dimension WL
is split into two series transistors, M1A and
M1B of size WL1
and WL2
respectively, where L = L1 +L2. The intermediate node X
is a low impedance node. The drain of the bottom transistor is connected to the
21
source of the top transistor while both gates are tied with each other. Now, while
in operation, the top transistor always operates in saturation and the bottom
one operates in triode. Similarly for the PMOS, the configuration is shown in
Fig. 2.15(b). The only significant difference is now the bottom transistor M2A is
in saturation and the top one, M2B is in triode.
NMOS Configuration PMOS Configuration
M1B NMOS operates in triodeM1B NMOS operates in triode M2B PMOS operates in triode
X is a low-impedance node Y is a low-impedance node(a) (b)
NMOS Configuration PMOS Configuration
L=L1+L2
Figure 2.15: Illustration of split-length transistors.
Now, personal communication with Furth lead to an interesting technique,
which improves the LDO performance. In this technique, we not only vary the
length of the transistors, but also the width of the transistors keeping the dimen-
sion as WL2
and mWL1
for the transistor in triode and saturation, respectively, where
L2 > L1. This is the main compensation technique that we used in our design
with some additional compensation techniques to have a stable system.
2.7 Split-Length Compensation
As discussed in the previous section, split-length transistors form an in-
termidiate low-impedence node. If any current is fed to this node through com-
pensation capacitors, than this path works as split-length compensation network.
Fig. 2.16 shows split-length compensation for NMOS transistor. The small signal
model for this compensation network is shown in Fig. 2.17
22
G
D
S
W/L
G
D
S
M1
M1A
M1B
CC
Ifb
X
mW/L1
W/L2
Figure 2.16: Illustration of split-length compensation for NMOS.
VX
Figure 2.17: Small signal model for split-length compensation for NMOS.
23
The transconductance, gm of a transistor of size WL
in strong inversion is
given by the equation
gm =
√µn · COX ·
W
L· ID (2.16)
For split-length compensation with varied width, transistor M1A is in sat-
uration and M1B is in deep triode. The transconductance gm1A and gm1B can be
found by the equations
gm1A =
√µn · COX ·
mW
L1· ID (2.17)
gm1B =
√µn · COX ·
W
L2· ID (2.18)
The input resistance at node X is given by
Rin =1
gm1A
|| 1
gm1B
(2.19)
2.8 Non-Overlapping Clock Generator Circuit
A clock generator input is a single clock but it produces two-phase non-
overlapping clocks. The schematic of the clock generator circuit is shown in
Fig. 2.18. A non-overlapping clock generator has a common turn OFF time be-
tween two transitions known as dead time and is shown in Fig. 2.19. Dead time
24
is created by incorporating the same number of delay cells between the input
and output clocks. The function of NAND gates is to make the signals non-
overlapping. To drive large capacitive load, a driver circuit is needed.
CLOCK
Phase 2 (φ2)
`
Delay cells
Figure 2.18: Schematic of a typical Non-overlapping clock generator [17].
25
Dead time Dead time Dead time Dead time
Ph
ase
1P
has
e 2
Time
Time
Figure 2.19: Output waveforms phase 1 and phase 2 of the non-overlapping clockgenerator [17].
26
Chapter 3
DESIGN AND SIMULATIONS
In this chapter, we discuss the detailed explanations of the proposed LDO. In the
beginning, we show the schematic of the proposed LDO. Discussion of its operation
follows. We also show other circuits that we make up to design the LDO. The
working principle of the charge pump and the non-overlapping clock generator are
also discussed in this chapter. An AC small signal model is also included here.
This chapter is concluded with load and line transient, PSR, Ripple and dropout
voltage measurement test benches and discussions of the simulation results.
3.1 Proposed Low-Dropout Voltage Regulators
We proposed two LDOs that are identical, except for the compensation.
The schematic is shown in Fig. 3.1. The two propsed designs are named LDO1
and LDO2. Device dimensions values are given in Table. 3.1.
As we can see from the schematic, it has an NMOS differential pair as the
first stage. Split-length transistors are used instead of single NMOS transistor.
The intermediate low impedence node of this configuration is used for compen-
sations. The second stage uses a single PMOS transistor as a common source
amplifier. This configuration helps to improve the output swing. At the output
stage, an NMOS pass element is in source follower configuration. The most inter-
esting part of this LDO is in between stage two and the output stage. A capacitor
CBATT that is fed by a charge pump is there. The charge pump actually works as
27
VREF
MBIAS M5
M1A
M1B
M2A
M2B
M3 M4 M6
M7
IBIAS
VDD
VSS
CHARGE
PUMP
VFB
VOUT
COUT
IL
MNPASS
V1
V02 VI3
VX
VY
VBIAS
FIRST STAGE SECOND STAGE OUTPUT STAGE
VFB
CBATT
Figure 3.1: Schematic for the proposed LDO.
a DC source to boost the gate voltage of the pass element. The main reason why
we used it is to get lower dropout voltage for the regulator.
3.2 Proposed LDO Regulator Architecture and Design
The schematics of the proposed LDOs showing compensation networks are
shown in Figs. 3.2 and 3.3. The first-stage has a split-length NMOS differential
pair, as discussed in Chapter 2. Both first and second stages are inverting. Miller
compensation RC and CC from the second stage output to the first stage output is
introduced. Another compensation network from the output of the second stage
is connected to the mid-point of the split-length differential pair through CC1.
Another capacitor CC2 was added from the output of the LDO to the mid-point
of the split-length differential pair. All the above statements hold true for both
28
Table 3.1: Device dimensions in µm for the LDO1 and LDO2.
LDO1 LDO2Transistors W
Lµm
M1A, M2A2
0.270, m=2
M1B,M2B1
0.450, m=2
M3,M43
0.540, m=2
M51
0.540, m=4
Mbias1
0.540, m=1
M63
0.540, m=10
M71
0.540, m=10
MPass30
0.180, m=200
CBATT 10 pF
LDOs except that RC1 was added in series to CC1 in LDO2. Also for LDO2, an
additional capacitor CC3 was added in the gate of the NMOS pass element. The
other end of the capacitor was grounded.
The dimensions for all devices in the compensation networks are shown in
Table 3.2.
Table 3.2: Component’s values used in both LDOs.
LDO1 LDO2
RC 200 kΩ
CC 500 fF
RC1 N/A 100 kΩ
CC1 3 pF
CC2 1.5 pF
CC3 N/A 10 pF
While designing, first step was to design a simple two-stage amplifier with
good gain. The amplifier was tested for stability. After tweeking the compensation
when the system was stable, the pass element was added to the design. A capacitor
CBATT was added in between the output of the second stage and input of the
29
output stage. This capacitor is used to boost the DC voltage with the help of a
charge pump.
It is assumed that the charge pump that will be designed to be capable
of boosting the DC voltage by approximately 800 mV. So, during simulations,
the capacitor has the condition that its initial voltage is 800 mV. The System is
also tested for stability. Compensations network is tweeked to make the system
stable. Upon finding the system to be stable, it is tested for dropout voltage.
The size of the pass element is kept as a variable. Tests are performed until the
desired dropout voltage is achieved. After fixing the pass element size, the LDO
is again tested for stability. If needed, compensation values are tweeked more to
achieve a stable system. Finally it is tested for all other performance parameter
like recovery time, line transient, load transient, PSR and dropout etc. And the
results are found to be closer to specifications.
VREF
MBIAS M5
M1A
M1B
M2A
M2B
M3 M4 M6
M7
IBIAS
VDD
VSS
CHARGE
PUMP
VFB
VOUT
COUT IL
MNPASS
RC CC
CC1
CC2
V1
V02 VI3
V11
VX
VY
VBIAS
FIRST STAGE SECOND STAGE OUTPUT STAGE
VFB
CBATT
Figure 3.2: Schematic of the Proposed LDO1 with Compensation Capacitor.
30
VREF
MBIAS M5
M1A
M1B
M2A
M2B
M3 M4 M6
M7
IBIAS
VDD
VSS
CHARGE
PUMP
VFB
VOUT
COUT
IL
MNPASS
RC CC
CC1
CC2
RC1
CC3
V1 VO2 VI3
V11
VX
VY
FIRST STAGE SECOND STAGE OUTPUT STAGE
VFB
CBATT
Figure 3.3: Schematic of the Proposed LDO2 with Compensation Capacitor.
3.3 Small Signal Analysis
The small signal architectures of LDO1 and LDO2 are shown in Figs. 3.4
and 3.5, respectively. The motivation for using this model is to analyze the DC
gain of each individual stage of the proposed LDOs and to conduct a thorough
pole-zero analysis.
3.3.1 First Stage
The first stage of the proposed LDO is a spilt-length NMOS differential
amplifer. The first stage provides a fair portion of the overall gain of the amplifier.
In this stage, we see a conversion from diffential input to single-ended output which
is achieved by current mirror M3 and M4. Current from M1A is mirrored by M3
to M4. This current is substracted from the current of M2A to create the single-
ended output. Now, with an increase in the feedback voltage VFB, the voltage at
the gate of the PMOS current mirror VY starts decreasing, resulting in an increase
31
-GM1 -GM2 +GMPASS
R1 C1 R2 C2 ROUT COUT
VIN VOUT
RC CC
+gM2A
1/g
M2A
1/g
M2B
CC1CC2
CBATT
V1 V2 V3
Figure 3.4: Small-signal architecture of LDO1.
of the voltage V1. On the other hand, if the feedback voltage VFB decreases the
voltage VY increases and then the voltage V1 decreases.
The first stage transconductance GM1 is given by,
GM1 =gM2A · gM2B
gM2A + gM2B
(3.1)
32
-GM1 -GM2
+GMPASS
R1 C1 R2 C2 ROUT COUT
VIN VOUT
RC CC
+gM2A
1/g
M2A
1/g
M2B
CC1CC2
RC
1
CBATT
C3
V1 V2V3
Figure 3.5: Small-signal architecture of LDO2.
where gM2A and gM2B are transconductances of the transistors M2A and M2B,
respectively. The output resistance R1 of the first stage is given by,
R1 = ro4 ‖(gM2A · ro2A ·
1
gM2B
)(3.2)
where ro4 is the output resistance of transistor M4 from node V1 to ground.(gM2A·
ro2A · 1gM2B
)is the output resistance of the split-length transistors M2A and M2B
33
looking from the drain of M2A to ground. Thus, the first stage gain AV 1 is given
by
AV 1 = GM1 ·R1 =
(gM2A · gM2B
gM2A + gM2B
)·(ro4 ‖ gM2A · ro2A ·
1
gM2B
)(3.3)
3.3.2 Second Stage
This stage has a PMOS transistor with an active load NMOS current
source. The PMOS transistor in this stage is configured in common source mode.
This configuration helps improve the output swing of stage two. This stage is an
inverting stage. The output V1 of the first stage is the input to the second stage
here. The output of this second stage is applied to the input of the charge pump.
The gain of the second stage is:
AV 2 = gM6 ·(ro6 ‖ ro7
)(3.4)
where gM6 is the transconductance of transistor M6 and r06 and r07 are the output
resistances looking into the drains of transistors M6 and M7, respectively. The
biasing circuit ensures a proper operating point so that the transistors are in
saturation region.
3.3.3 Gain in Level Shifter
The capacitor CBATT which is connected with a charge pump has a DC
gain. This gain is basically a voltage divider in capacitors. The gain formula is
AV 3 =CBATT
CBATT + C3
(3.5)
34
where for LDO1 C3 is the gate to source parasitic capacitance of pass transistor.
This capacitance is negligible in comparison with CBATT , hence the gain is unity.
For LDO2, this parasitic capacitance is negligible with respect to actual C3.
3.3.4 Output Stage
The output stage of the proposed LDO is a common drain amplifier, also
known as a source follower. This transistor is called the pass element and con-
sidered the most important part of the LDO. The gate or the input of the pass
element is connected to the high voltage side of the capacitor CBATT . The drain
of the pass element is connected to the supply voltage. The source of the NMOS
pass element is the output node.
To achieve a low dropout value, the gate voltage of the pass element needs
to be higher than the supply voltage. The charge pump does the job. The input
resistance of the output stage is very high, therefore, no current passes through
the input. And the output resistance of the source follower is very low which
means it can be driven at high loads. All the load current comes from the supply
voltage through the drain to the source. This drain current or load current is
a direct function of VGS along with some transistor parameter. Therefore, for
a fixed load current, if the gate voltage increases, and the load current cannot
be changed, then the source voltage must increase. This is the trick we pick for
designing low drop out. If we can increase the gate voltage of the pass element
to a high value, we can easily get a very low dropout from this regulator. As this
stage is basically a buffer stage, it does not contribute in voltage gain.
Ignoring the body effect, the gain equation of this stage can be written as:
AV O =
(gMPASS
gMPASS + 1rOPASS
)≈ 1 (3.6)
35
If we include the body effect, the gain equation can be written as:
AV O =
(gMPASS
gMPASS + gmb + 1rOPASS
)< 1 (3.7)
where gmb is the backgate transconductance, and is defined as the change in drain
current due to change in backgate bias voltage [18].
Typically, under no load conditions, AV O=0.8 V/V [19].
The overall gain of the LDO is
ALDO = AV 1 · AV 2 · AV 3 · AV O (3.8)
3.3.5 Charge Pump Operation
A charge pump is a type of DC-DC converter. It can increase or decrease
a DC voltage using capacitors and switches. Because the NMOS pass element
needs a voltage higher than the supply voltage for proper functioning, a charge
pump is introduced to the LDO cuicuit. One of the design constraints is that, no
current can be drawn from VREF . In addition, if VREF is held at zero, the charge
pump will not charge.
The charge pump needs one capacitor, four NMOS and one PMOS tran-
sistor. The schematic of the proposed charge pump is shown in Fig. 3.6. One
of the NMOS transistors MC5 is used as switch. Capacitor CF is a flying ca-
pacitor. CBATT is the reservoir capacitor. One of the NMOS transistors MC2 is
connected such that it forms a diode. The final PMOS MC3 and NMOS MC4 are
used as transmission gate switch. Reason we use transmission gate switch here is
beacause, VO2 range is wide, and transmission gate allows both strong and weak
signals to pass through it undegraded. Sizes used for all the MOSes were mini-
mum size. Typically the flying capacitor CF , is 10 times smaller than the reservoir
36
CBATT . The flying capacitor is used for charging up the reservoir capacitor, which
works as a battery in the amplifier.
Designing transistor MC1 is tricky. It behaves as a diode-connected tran-
sistor attached to VREF . The drain terminal however, is attached to VDD so that
no current is drawn from VREF . We could have connected VDD instead of VREF
to the gate terminal. We would have gotten a higher voltage from the charge
pump. But the system would have shown poor noise rejection from VDD. We also
could have connected the drain terminal to VREF , but the design would not only
produce lower output voltage but also draw current from VREF . So, our trade-off
is to connect the drain terminal to VDD.
During phase one, as shown in Fig. 3.7(a), when φ1 is high, the lower
terminal of the flying capacitor CF is pulled down to zero. Because VREF is
connected to the gate of the NMOS MC1, it will be ON and the source of this
transistor will charge to the voltage of VTHN below VREF . Now during phase two,
as shown in Fig. 3.7(b), when φ2 is high and φ1 is low, MC5, will be OFF. The
charge pump input VO2 will be applied to the lower terminal of the CF through
transmisson gate switch. Due to the property of the capacitor, the other end
of capacitor CF will change drastically to maintain the same potential difference
between the terminals, resulting in a higher voltage at the upper terminal of the
flying capacitor. Now, NMOS MC2 is configured as a diode. The higher voltage
at the capacitor terminal will make MC2 forward biased and current will flow
through the diode to charge the reservoir capacitor CBATT . Then again, when
we return to phase φ1, the higher voltage at the upper terminal of the reservoir
cannot be discharged because of the reverse biased diode MC2. So the capacitor
holds charge until it finds an external discharging path.
The dimensions used for the charge pump are given in Table. 3.3
37
MC1
VSS
VDD
VREF
VO2
VI3
MC2MC3MC4
MC5
CF
CBATTMNPASS
VDD
CHARGE PUMP
PHI1PHI2 PHI2B
Figure 3.6: Schematic of the designed Charge Pump.
Table 3.3: Device dimensions in µm for Charge Pump.
Transistors WLµm
MC1, MC20.6000.180
MC4, MC50.6000.180
M31.2
0.180
CF 500 fF
3.3.6 Non-overlapping Clock Genarator Design
To avoid charge sharing of the capacitors in the charge pump, two non-
overlapping clock signal Φ1 and Φ2 are required. These two signals Φ1 and Φ2 are
generated with a dead time of 8 ns. The schematic of the clock generator circuit
38
(a) (b)
Figure 3.7: Charge Pump operation.
is shown in Fig. 3.8. Eight inverters and seven resistors are needed in each path
of the clock generator to achieve the required dead time. Two more inverters are
used in each path as the driver circuit. There is one more inverter at the clock
input. This inverter adds additional delay in the respective path of the clock
generator. To compensate for this delay, a transmissation gate of the same size is
introduced into the other path of the circuit.
Series inverters and resistors contribute to the desired delay in the output
because of the RC time constant of the circuit. The RC time constant can be
tuned by changing C or R values. In this design, we increase R more rather than
C to get our required delay. The reason to use a higher resistance is that dynamic
power consumption is a function of capacitance. For any switching circuit, the
dynamic power consumption is a function of frequency given by
39
PDYN = C · V 2 · fop (3.9)
where C is the capacitance, V is the applied voltage and fop is switching frequency.
Inverters used in the design were multiplicity 1 and resistors were 500k Ω.
The clock generator was tested with 10 kHz clock and the result was found to be
very close to the design value.
Ths dimension used for the non-overlapping clock generator is shown in
Table. 3.4
Table 3.4: Device dimensions in µm for Non-overlapping Clock Generator.
Devices WL
RCLK 500 kΩ
INV X11.2
0.180,
PMOS
0.6000.180
,NMOS
TG 1.20.180
,PMOS
0.6000.180
,NMOS
NAND 1.20.180
,PMOS
1.20.180
,NMOS
3.3.7 Poles and Zeros
The LHP dominant pole ωP1 & ωP2 for LDO1 can be found at
ωP1 = − gM2A + gM2B
gM2 · gM2B ·R1 ·R2 · (CC1 + CC2 · AV3)(3.10)
ωP2 = − 1
ωP1 · CC2 ·ROUT · COUT ·R1 · AV2(3.11)
40
VDD
SW1
SW2
SW2B
A
B
NAND
CLK
VSS
TG
SW1B
A
B
NAND
INVX1
500k
Delay Cell Delay Cell
500k
INVX1
Figure 3.8: Schematic of the designed non-overlapping clock generator, which uses7 delay cells in each path.
The LHP dominant zero ωZ1 for LDO1 is found at
ωZ1 = − gM2A+gM2B
CC1·(1+gM2B
gMPASS)+CC2
3.4 Simulation Results
In this section of the chapter, AC analysis, dropout voltage measurement,
line and load transient responses and power supply rejection results are shown
and discussed.
3.4.1 AC Analysis
The AC test bench for the two designs is shown in Fig. 3.9. A current
mirror is used to provide load current IL to the output of the LDO. Sizes of the
transistors are carefully designed to handle the huge load current of 100 mA. The
41
transistors in the current mirror are in ratio of 4 : 1. The impedence of a single
bonding wire of an IC is modeled as 1.37 nH inductor in series with 100 mΩ
resistor and the capacitance is 120 fF, as is shown in Fig. 3.9. Eight such parallel
models are connected to the input and output of the LDOs because the number of
pins used is eight each for both input and output. In this test bench, the battery
capacitor is configured such that its initial voltage value is 800 mV. The charge
pump is omitted.
The only difference between the test benches is, for LDO1 we use four
input pins and two output pins. On the other hand, for LDO2, all eight input
pins and output pins are used.
An AC input source with a magnitude of 1 V and a phase of 180o is placed
to perform the AC analysis. A capacitor of 1 F is used for injecting the AC input
signal to the LDO. A large resistor of 1 GΩ is used to the break the feedback loop
of the LDO from VOUT to the negative V− terminal of the error amplifier.
LDO1 and LDO2 are simulated at both minimum and maximum load
currents of 3 µA and 100 mA, respectively. Simulated AC results of LDO1 are
shown Fig. 3.10. The LDO2 simulated AC results are shown in Fig. 3.11. AC
analysis comparison of LDO1 and LDO2 at minimum load current IL,min=3 µA
and maximum load current IL,max=100 mA is given in Table. 3.5.
Table 3.5: AC analysis for LDO1 and LDO2 Regulator at IL,min = 3µA andIL,max = 100 mA.
LDO1 Regulator LDO2 RegulatorIL 3µA 100 mA 3µA 100 mAGain 66.6 dB 66.74 dB 66.6 dB 66.74 dBGM 50.57 dB 25.71 dB 15.62 dB 38.68 dBPM 49.17 91.3 57.52 91.94
fUGF 263.2 kHz 430.2 kHz 297.7 kHz 784.5 kHz
42
AC
12.5 mΩ
0.171 nH
12.5 mΩ
0.171 nH
LDO
VIN
VREF
1 F 1 GΩ
CL
IBIAS
VDD
IL/4
IL5
0 Ω
50
Ω
VOUT
VSS
96
0 f
F
10
0 p
F
96
0 f
F
VDD
Ro
utm
ax
8 Parallel I/O Pads
and Bonding Wires
8 Parallel I/O Pads
and Bonding Wires
AC open-loop
4:1
Figure 3.9: Testbench for AC analysis.
From Table. 3.5, we see that the unity gain frequency fUGF increases as IL
increases. Phase Margin (PM) also increases as IL increases. The gain is identical
for the two designs because only compensation is different. Results show improved
AC performance of LDO2 over LDO1.
3.4.2 Dropout Voltage Measurement
The test bench for dropout measurement is shown in Fig. 3.12. Like the
AC analysis, this test bench also has the same value for equivalent series inductors,
resistors and equivalent capacitors based on the number of pads used. In the case
43
Figure 3.10: LDO1 AC analysis.
of dropout measurement, a triangular input VIN with a very slow rise and fall
times of 25 ms is applied. The dropout is measured at the maximum load current
IL,max=100 mA. Initially the dropout voltage was measured using a battery in
place of CBATT . The battery voltage was set to 800 mV. After the dropout test,
the battery was replaced by CBATT and a charge pump in simulation. The charge
pump was expected to deliver an 800 mV difference in the DC voltage between
the output of the second stage and the input of the third stage. And the system
was again tested for dropout voltage.
44
Figure 3.11: LDO2 AC analysis.
Dropout voltage comparison for both LDO’s at maximum load current
IL,max = 100 mA is shown in Table. 3.6. The measured dropout voltages using
the battery are 62 mV and 39 mV, respectively for LDO1 and LDO2 which are
within our specifications. And the measured values for dropout are 202 mV and
121 mV, respectively for LDO1 and LDO2 with CBATT and charge pump. The
difference is significant, roughly three times higher than expected.
45
0.171 nH
0.171 nH
LDO
VREF
CL
IBIAS
VDD
IL/4
IL
50
Ω
50
Ω
VOUT
VSS
Tri
ang
ula
r P
uls
e w
ith
rise
an
d f
all
tim
e 2
5 m
s
VFB
96
0 f
F
10
0 p
F
96
0 f
F
VDD
Routm
ax
8 Parallel I/O Pads
and Bonding Wires
8 Parallel I/O Pads
and Bonding Wires
4:1
12.5 mΩ
12.5 mΩ
Figure 3.12: Test bench for dropout voltage simulation.
Table 3.6: Simulated dropout voltage for LDO1 and LDO2 at maximum load withand without the charge pump and the capacitor CBATT .
LDO1 LDO2
VDO with battery 62 mV 39 mVVDO with CBATT and CP 202 mV 121 mV
46
3.4.3 Line Transient
The testbench for line transient analysis is given in Fig. 3.13 with the same
differences between the two designs, as discussed in earlier test benches. A current
source was used as the load so that the output current is constant. The input
voltage, VIN was varied from 1.5 V to 1.8 V with rise and fall times of 10 ns while
the load current, IL was kept constant at 1 mA during this test. The line transient
responses for LDO1 and LDO2 are shown in Figs. 3.14 and 3.15, respectively.
Rise time tRH,Line, fall time tRL,Line, ∆VOUT,Line, overshoot and undershoot of line
transient response for both designs are shown in Table. 3.7. From the table we see
that, although LDO1 has higher overshoot and undershoot, the recovery time is
faster than LDO2. Line regulation of LDO1 is roughly twenty times smaller than
LDO2. But total change in VOUT during the line transient of LDO2 is almost half
that of LDO1.
Why the line transient of LDO2 is much better than that of LDO1? The
answer is the capacitor C3. For LDO2 this extra capacitor holds the charges for
a longer time. During transient analysis, when the input voltage changes, the
output voltage tends to follow the input, but the gate of the pass transistor gets
enough voltage from C3 to make the transistor on, resulting smaller overshoot and
undershoot than LDO1.
Table 3.7: Line transient simulation results for LDO1 and LDO2 regulators.
LDO1 LDO2
tRH,Line 1.6 µs 2.99 µs
tRL,Line 2.4 µs 3.84 µs
∆VOUT,Line 310 mV 159.5 mV
Overshoot 200 mV 81.06 mV
Undershoot 110 mV 78.5 mV
Line Regulation 0.3 mV/V 6.7 mV/V
47
0.171 nH
0.171 nH
LDO
VREF
CL
IBIAS
VDD
IL/4
IL
50
Ω
50
Ω
VDD
VOUT
VSS
Pu
lse
wit
h r
ise
and
fal
l
tim
e 1
0 n
s
VFB
96
0 f
F
10
0 p
F
96
0 f
F
8 Parallel I/O Pads
and Bonding Wires
4:1
Ro
utm
ax
8 Parallel I/O Pads
and Bonding Wires
12.5 mΩ
12.5 mΩ
Figure 3.13: Test bench for line transient simulation.
48
Figure 3.14: Line Transient Response for LDO1.
49
Figure 3.15: Line Transient Response for LDO2.
50
3.4.4 Load Transient
A testbench for load transient analysis is given in Fig. 3.16. The number
of input and output pins determines the equivalent inductance, resistance and
capacitance values associated with each pad/pins. The load current IL varies
from 3µ A to 100 mA with a rise time of 10 ns and fall time of 10 ns while the
input voltage, VIN stayed at 1.5 V throughout this test. As shown in the test
bench, the maximum load current is drawn from VOUT which is mirrored by a
current source so that for any overshoot or undershoot, the output current does
not change. The minimum load current is drawn by a 400 kΩ resistor. Only the
maximum load current was switched on and off to create the load variations.
The load transient response for both LDO’s are shown in Figs. 3.17 and
3.18. tRH,Load, tRL,Load, ∆VOUT,Load, overshoot and undershoot of load transient
response for both designs are summarized in Table. 3.8.
From the simulated results, we see that recovery times and load regula-
tion are almost same for both LDOs but there is a significant difference in total
load transient values. Total load transient value is lower for LDO2 than LDO1.
Although overshoots are almost same for both LDOs, there is a significant im-
provement in undershoot for LDO2. LDO2 is performing better than LDO1 if
load transient test is considered.
Why LDO2 has a better undershoot value than LDO1? The answer is
again the capacitor, C3. This capacitor holds the gate voltage. When load current
increases from 3 µA to 100 mA, the source of the pass transistor starts to decrease
to accomodate higher current. Because the capacitor C3 holds the charges, the
gate voltage remains high, which resists the source voltage to go to a low value.
Already we know that this source voltage is our output voltage.
51
0.171 nH
0.171 nH
LDO
VREF
CL
IBIAS
VDD
RL
IL
50 Ω
50 Ω
VL
VOUT
VSS
Pulse such that IL rise
and fall time is 10 ns
VFB
VIN 960 f
F
100 p
F
960 f
F
Routm
ax
8 Parallel I/O Pads
and Bonding Wires
8 Parallel I/O Pads
and Bonding Wires4:1
12.5 mΩ
12.5 mΩ
Figure 3.16: Testbench for load transient simulation.
Table 3.8: Load transient simulation results for LDO1 and LDO2 regulator.
LDO1 LDO2
tRH,Load 16 µs 16 µs
tRL,Load 5.2 µs 7 µs
∆VOUT,Load 879 mV 668 mV
Overshoot 300 mV 297 mV
Undershoot 579 mV 371 mV
Load Regulation 0.02 mV/mA 0.0198 mV/mA
52
(b)
Figure 3.17: LDO1 load transient response.
53
Figure 3.18: LDO2 load transient response.
54
3.4.5 Ripple
Fig. 3.19 shows the test bench for measurement of ripple for both LDOs.
A direct connection from VOUT is drawn to the negative input terminal of the
error amplifier. A constant voltage of 1.5 V is applied as the input. A transient
simulation is run. The test is performed for different load current, and the ripple
is found to be the same.
0.171 nH
0.171 nH
LDO
VREF
CL
IBIAS
VDD
IL/4
IL
50
Ω 50
Ω
VDD
VOUT
VSS
VFB
96
0 f
F
10
0 p
F
96
0 f
F
8 Parallel I/O Pads
and Bonding Wires
4:1
Ro
utm
ax
8 Parallel I/O Pads
and Bonding Wires
VDD
12.5 mΩ
12.5 mΩ
Figure 3.19: Test Bench for Ripple measurement.
Clock is the source of ripple in the LDO. When there is a transition in
clock, ripple can be observed in the output. If clock is removed, ripple goes away.
The measured values of ripple are shown in Figs. 3.20 and 3.21 for LDO1 and
LDO2, respectively. As seen from the figures, LDO2 has lower ripple voltage
(0.6 mV) than LDO1 (1.6 mV) and is almost three times smaller.
55
Figure 3.20: Ripple measurement for LDO1 at Load Current = 1 mA.
3.4.6 Power Supply Rejection
Fig. 3.22 shows the test bench for measuring power supply rejection (PSR).
A direct connection from VOUT is given to the negative terminal of the error
amplifier. In the input signal, noise is introduced with the help of an AC voltage
source. An AC supply is connected in series with the DC supply voltage VDD.
Our goal is to find how much AC signal we receive at the output for different
frequencies. AC analysis is run in Spectre. PSR is measured for a load current of
IL=1 mA. PSR is defined as
PSR = 20 · log(VDD,AC
VOUT
)(3.12)
56
Figure 3.21: Ripple measurement for LDO2 at Load Current = 1 mA..
The PSR results are shown in Figs. 3.23 and 3.24 for both LDO1 and
LDO2. As seen from the figures, PSR is very good at low frequencies, and as
frequency increases, the PSR drops. It was found that, within the unity gain
frequencies of the LDOs, the PSR values are 16 dB for LDO1 and 14 dB for
LDO2. We also see that, PSR curves of LDOs follows AC gain curves. We can
conclude that PSR values are roughly the AC gain plus 16 dB or 14 dB for LDOs
at high frequency. At low frequency, PSR value are the same for both LDOs.
57
0.171 nH
0.171 nH
LDO
VREF
CL
IBIAS
VDD
IL/4
IL
50
Ω 50
Ω
VDD
VOUT
VSS
VFB
96
0 f
F
10
0 p
F
96
0 f
F
8 Parallel I/O Pads
and Bonding Wires
4:1
Ro
utm
ax
8 Parallel I/O Pads
and Bonding Wires
AC
VDD
12.5 mΩ
12.5 mΩ
1 V 00Phase
Figure 3.22: Test Bench for PSR measurement.
58
Figure 3.23: PSR waveform for LDO1.
59
Figure 3.24: PSR waveform for LDO2.
60
Chapter 4
EXPERIMENTAL RESULTS
The layout techniques used for LDO1 and LDO2 are discussed here. A microscopic
view of the IC is shown in this chapter along with major hardware results of LDO1
and LDO2.
4.1 Layout
Both chips were fabricated in 0.180 µm IBM 7 RF technology and packaged
in QFN-40 packages through MOSIS. A microscopic view of the LDO1 is shown
in Fig. 4.1. Almost nothing can be seen except for the metal 6 layer.
The layouts of LDO1 and LDO2 are shown in Figs. 4.2 and 4.3, respectively.
The total area of the two designs, area of the pass transistor and total capacitance
are shown in Table 4.1. LDO1 is also shown in Fig. 4.4 with the 40-pin pad frame.
29 pins are used for testing the LDO. 3 pins are left empty. The remaining 8 pins
are used for testing the charge pump and a resistor layed out in the IC. The same
configuration is used for LDO2.
The common-centroid technique is used to ensure good matching of both
NMOS and PMOS transistors. Common-centroid was mainly applied to differen-
tial pairs and current mirrors. The layout area of the two LDO designs are the
same except for the LDO2 has an additional 10 pF capacitor and 100 kΩ resistor.
4.1.1 Passive Elements Layout
Several capacitors and resistors were layed out in the IC, which are mainly
used in the compensation network, charge pump and clock generator. Five capac-
61
Figure 4.1: Microscopic view of LDO1 (Die measure 1.5 mm x 1.5 mm).
itors were used of size 10 pF, 3 pF, 1.5 pF, 500 fF and 100 fF. One of the beauty
of the IBM 7 RF tool kit is that it automatically creates the layout. We need to
choose only the dimensions. We used the MIM capacitor which uses metal layers 6
and 7. Resistors are also layed out automatically and we need to choose only the
dimensions. Three resistors are layed out in the IC of values 500 kΩ, 200 kΩ and
100 kΩ. We use oprrpres (the high-resistance polisilicon resistor) resistors.
Figs. 4.5 and 4.6 show layouts of a 10 pF capacitor and 200 kΩ resistor.
4.1.2 Pass Element Layout
The layout of the pass element is challenging. The width of the NMOS
pass element is 6 mm. It is a mammoth transistor. It is layed out block by block.
The first step is to layout a transistor with a width of 300 µm. Then connect four
identical 300 µm transistors with drains and sources shared, which results in a
62
Table 4.1: Layout Area for LDO1 and LDO2 regulators and Components.
LDO1 LDO2
Pass Element 44.84 µm x 127.17 µm
Error Amplifier 30.11 µm x 15.15 µm
Cap 10 pF 74 µm x 73.87 µm
Cap 3 pF 42.35 µm x 42.35 µm
Cap 1.5 pF 31.14 µm x 31.15 µm
Cap 500 fF 19.71 µm x 19.72 µm
Resistor 500 k 44.84 µm x 127.17 µm
Resistor 200 k 21.85 µm x 23.14 µm
Resistor 100 K 21.85 µm x 11.29 µm
Charge Pump 95.64 µm x 74 µm
Clock Generator 155.55 µm x 137.24 µm
Total Area of Components 38484 µm2 43950 µm2
1.2 mm transistor. Five rows of 1.2 mm transistor are then connected to get the
whole 6 mm pass transistor. Because the LDO is designed for 100 mA maximum
load current, the source and drain of the pass element are made very thick and
three layers of metal are used. For better connectivity of the gate, metal 2 is used
to strap the poly layer. Fig. 4.7 shows the layout of the NMOS pass element.
4.1.3 Layout of Other Circuits
The error amplifier has a split-length NMOS differential with a PMOS
current mirror load, bias circuitry and an output PMOS transistor in common-
source configuration with an NMOS current source load. The NMOS differential
pair, PMOS current mirror, all the biasing circuits and the second-stage PMOS
common-source amplifier, were all layed out using the common centroid technique
for better matching. Once all the transistors are connected properly, compensation
networks are added to respective ports.
63
Figure 4.2: Layout of LDO1 (Dimension 275 µm x 437 µm).
The charge pump consists of five transistors of unit size and two capacitors
of 10 pF and 100 fF. The function of the charge pump is to take the error am-
plifier output as input and boost the value so that the pass element can have the
necessary voltage it needs to operate the LDO properly. The first step of laying
out the charge pump is placing two capacitors. They take considerable space.
Then the rest of the transistors are placed in the empty spaces between the two
capacitors and connected properly with metal layers.
64
Figure 4.3: Layout of LDO2 (Dimension 424 µm x 437 µm).
A non-overlapping clock generator with one input clock but two output
clocks is designed and layed out. There is a common turn off time between the
two phases of the clock outputs which is known as dead time. The clock generator
has a series of resistors and inverters which generate the necessary delay for the
dead time, a driving cell and NAND gates. The designed and layed out clock
generator has a dead time of 8 ns. While laying it out, the first step is to layout a
resistor and an inverter. Then connect seven such blocks together for each path.
The driver circuit, transmission gate and NAND gates are layed out and connected
with metal 1 and metal 2.
65
Figure 4.4: Layout of LDO1 with 40-pin pad frame (1.5 mm x 1.5 mm).
4.2 Hardware Results
LDO1 is tested on a bread board with the help of a 40 pin QFN to DIP
converter. For LDO2, a custom made Printed Circuit Board (PCB) was designed.
The reason to design a PCB over a bread board is that the PCB offers less parasitic
capacitance than that of a breadboard. The test procedure for LDO2 is described
in Appendix A. The same bias current Ib = 200 nA is used for both LDO1 and
LDO2. The 100 pF output load capacitance, CL, is not layed-out on chip. A
capacitor of 90 pF is used as the load capacitor CL. The parasitic capacitance
of the probes is about 10 pF, making the total load capacitance 100 pF. All the
66
Figure 4.5: Layout of 10 pF Capacitor.
connections are the same for both designs. For testing using the bread board, the
connections are changed manually, keeping all of the component values the same.
4.2.1 Dropout Voltage
The dropout voltage measurement for LDO1 and LDO2 are shown in
Figs. 4.8 and 4.9, respectively. Matlab is used for plotting these waveforms.
Dropout is measured at the maximum load current IL = 100 mA. At IL = 3 µA
the dropout value is almost zero. The clock frequency used to test the dropout
was 40 kHz. The load capacitor is 100 pF. To ensure a biasing current IBIAS of
200 nA, a resistor of appropriate value is used. Dropout is measured using
VDO = (VIN − VOUT ) |VOUT=VOUT,MAX−VOUT,MAX∗5% (4.1)
67
Figure 4.6: Layout of 200 kΩ resistor.
Table 4.2: Experimental dropout voltage for LDO1 and LDO2 at maximum load.
LDO1 LDO2Vdo 177 mV 82 mV
Table 4.2 shows the measured dropout voltages for LDO1 and LDO2. We
see that LDO2 has much better dropout (82 mV) than that of LDO1 (177 mV).
4.2.2 Ripple Measurement
Figs. 4.10 and 4.11 show a zoomed area for measuring the ripple of LDO1
and LDO2, respectively. Ripple is found to be independent of load current. In
this test, ripple is measured for a load current of 1 mA. The clock is responsible
for any ripple in the output. During every clock transition, ripple is observed at
the output. If we disconnect the clock, the ripple goes away. During this test,
68
Figure 4.7: Layout of NMOS Pass Element (Dimensions 44.65 µm x 127.97 µm).
a fixed input of 1.5 Volts is supplied to the LDOs. Ripple values are 9 mV and
3.8 mV, respectively, for LDO1 and LDO2.
4.2.3 Line Transient Response
Figs. 4.12 and 4.13 show the measured line transient response for LDO1
and LDO2, respectively. For the line transient measurement, the line voltage VIN
varies between 1.5 V to 1.8 V with equal 18 ns rise (trise) and fall (tfall) times.
Rise and fall times in Rigol DG4102 function generator can not be lowered below
10 ns. Because of the parasitic capacitance the rise and fall times are found to be
18 ns. Rise and fall times are measure from 0% to 100%, rather than from 10%
to 90% or 20% to 80%.
During the line transient test the load current IL stays at 1 mA. The test
procedure for the line transient is described in Appendix A. A load capacitor of
69
Figure 4.8: LDO1 Dropout Voltage Measurement.
100 pF is used for this testing. The measured data is averaged over 512 samples
using the oscilloscope and plotted using MATLAB. Averaging is used to remove
clock ripple, and 60 Hz noise coming from the elecctronic equipment. Overshoot,
undershoot, settling times and total output variation ∆VOUT are given in Ta-
ble 4.3.
70
Figure 4.9: LDO2 Dropout Voltage Measurement.
Table 4.3: Line transient experimental results for proposed LDOs.
LDO1 LDO2
tRH,Line 1.5 µs 1.9 µs
tRL,Line 2.2 µs 2.5 µs
∆Vout,Line 340 mV 162 mV
Overshoot 224 mV 90 mV
Undershoot 126 mV 72 mV
Line Regulation 1 mV/V 6.7 mV/V
71
Figure 4.10: Waveform for measuring Ripple for LDO1.
72
Figure 4.11: Waveform for measuring Ripple for LDO2.
73
Figure 4.12: Line Transient Response for LDO1.
74
Figure 4.13: Line Transient Response for LDO2.
75
4.2.4 Load Transient Response
Figs. 4.14 and 4.15 show the measured load transient response for LDO1
and LDO2, respectively. For the load transient analysis, the load current IL varies
between 3µA to 100 mA. During the load transient test, the input voltage VIN
stays at 1.5 V. The test procedure for the load transient is described in Appendix
A. A load capacitor of 100 pF is used. The measured data is averaged over 512
samples using the oscilloscope and plotted using MATLAB. Overshoot, under-
shoot, settling times and total output variation ∆VOUT are given in Table. 4.4.
Figure 4.14: Load Transient Response for LDO1.
4.2.5 PSR Measurements
Figs. 4.16 and 4.17 show the measured PSR waveform versus frequency.
In this test, an AC signal is connected in series with the supply voltage. The
76
Figure 4.15: Load Transient Response for LDO2.
Table 4.4: Load transient experimental result for proposed LDOs.
LDO1 LDO2
tRH,Load 7 µs 16 µs
tRL,Load 2.6 µs 7 µs
∆Vout,Load 1042 mV 610 mV
Overshoot 416 mV 210 mV
Undershoot 626 mV 305 mV
Load Regulation 0.02 mV/mA 1.0 mV/mA
amplitude of the AC signal is 300 mV (peak to peak) and the supply voltage is
fixed at 1.65V so that the input voltage of the LDO remains within its regulating
range. During this test, the load current is set at 1 mA. With the help of an
77
oscilloscope, the AC portion of the output voltage is measured. PSR is calculated
using the formula
PSR = 20 logInput
Output(4.2)
PSR at low frequency is very high, but as the frequency increases, the PSR
value decreases. At the unity gain frequency fUGF , PSR is found to be the same
for both LDO’s.
78
Figure 4.16: PSR waveform for LDO1.
79
Figure 4.17: PSR waveform for LDO2.
80
Chapter 5
DISCUSSION AND CONCLUSION
In this chapter, the simulated and measured results of the designed LDOs are
discussed. A comparison with several existing designs is provided. Finally, future
work is suggested in this chapter.
5.1 Result Comparison : Simulated vs. Measured
Major test results for LDO1 and LDO2 are summarized in Tables 5.1
and 5.2, respectively. The tables only list the simulated and measured results
of the LDOs. Although we also simulated the LDOs with a battery, instead of
with a capacitor and charge pump, the only change in simulated results occured
for dropout voltage. Other than that, there was no difference between the results
of simulation with a battery and the results of simulation with a capacitor and
charge pump. To calculate % error, we used,
Mismatch =Measured− Simulated
Simulated× 100% (5.1)
Tables 5.1 and 5.2 show that there are some variations between simu-
lated results and measured results. In some cases, measured values are smaller
than simulated values, in some cases, simulated values are smaller than measured
values. For instance, the measured dropout voltages are smaller than simulated
voltages for both LDOs. But measured ripple values are very high in comparison
with simulated ripple values. Measured line and load transient settling times are
81
either smaller than or equal to simulated values. Measured total change in VOUT
in both line and load transient for LDO1 is higher than that of simulated results.
On the other hand, for LDO2, measured total change in VOUT in load transient is
smaller than the simulated value.
The mismatch between simulated and measured results can be caused by
noise from the environment, normal process parameter tolerances, and test setup
and equipment. For instance, the power supply, measurement probe, and func-
tion generator all contribute noise at 60 Hz. Moreover, they have built-in parasitic
capacitance and resistance. All these parasitic capacitances and resistances can
affect the results of the LDOs. And process variation occurs for layed-out com-
ponents. For example, we haved layed-out a 500 kΩ resistor on the chip for test
purpose. When we measured the value with the help of a DMM, the values we
measured were 464 kΩ, 470 kΩ and 460 kΩ. This normal variation occurs for all
on chip resistors and capacitors that we have designed and used in the system.
Moreover, transistor mismatch can contribute in results variation. Metal routing
and contacts contributes parasitic capacitance and resistance of designed values
against layed-out values.
Using Tables 5.1 and 5.2 we can also compare LDO1 and LDO2. We see
a significant improvement in LDO2 in terms of dropout voltage, total variation
in VOUT in line and load transient. However, considering load regulation alone,
LDO1 performs better than LDO2.
Table 5.3 shows the dropout voltage result summary for both LDOs. From
the table, we see that simulated dropout voltages with the battery instead of a
capacitor and charge pump are very low. In contrast, simulated results with a
capacitor and a charge pump and measured results, are roughly three times larger.
82
Table 5.1: Results Comparison for LDO1.
Simulated Measured Mismatch(%)
Dropout Voltage 202 mV 177 mV −12.4
Ripple 1.82 mV 9 mV 374
Line Regulation 0.3 mV/V 1 mV/V 233
OvershootLine 200 mV 224 mV 12
UndershootLine 110 mV 126 mV 14.5
tRH,Line 1.6 µs 1.5 µs −6.2
tRL,Line 2.4 µs 2.2 µs −8.3
∆Vout,Line 310 mV 340 mV 9.7
Load Regulation 0.02 mV/mA 0.02 mV/mA 0
OvershootLoad 300 mV 416 mV 38.6
UndershootLoad 579 mV 626 mV 8.1
tRH,Load 16 µs 7 µs −56.2
tRL,Load 5.2 µs 2.6 µs −50
∆Vout,Load 879 mV 1042 mV 18.5
PSR at fUGF 16 dB 13 dB −18.7
The error in the dropout voltage simulation result was not known until
after measuring the fabricated chips. Due to a memory limitation of the server,
simulations including the capacitor and charge pump of the dropout voltage, were
not possible. Because all other results matched for both simulations (with the
battery or with the capacitor and charge pump), it was thought to be the same.
After analysing the charge pump, the problem was discovered.
. Fig. 5.1 is included here again for better understanding. Looking back
at the description of charge pump operation in Chapter 3, during phase one,
the voltage at the upper terminal of the flying capacitor is charges to value one
VGS below the VREF . Because the charge pump clock cycles are so long, we
assumed VGS= 0.2 V and VREF=1.2 V, respectively, resulting in 1000 mV across
the flying capacitor. As such, during phase two, we expect the gate voltage of the
83
Table 5.2: Results Comparison for LDO2.
Simulated Measured Mismatch(%)
Dropout Voltage 121 mV 82 mV −32.2
Ripple 0.6 mV 3.8 mV 533
Line Regulation 6.7 mV/V 6.7 mV/V 0
OvershootLine 81.06 mV 90 mV 11
UndershootLine 78.5 mV 72 mV −8.2
tRH,Line 2.99 µs 1.9 µs −36.4
tRL,Line 3.84 µs 2.5 µs −34.9
∆Vout,Line 159.5 mV 162 mV 1.5
Load Regulation 0.0198 mV/mA 1.0mV/mA 4950
OvershootLoad 297 mV 210 mV −29.2
UndershootLoad 371 mV 305 mV −17.7
tRH,Load 16 µs 16 µs 0
tRL,Load 7 µs 7 µs 0
∆Vout,Load 668 mV 610 mV −8.6
PSR at fUGF 14 dB 13 dB −7.1
Table 5.3: Simulated dropout voltage for LDO1 and LDO2 at maximum load.
LDO1 LDO2
VDO with battery 62 mV 39 mVVDO with CP 202 mV 121 mVVDO measured 177 mV 82 mV
pass transistor to be 800 mV above the output of the second stage of the error
amplifier after a drop of approximately 0.2 V across MC2. Transistors MC1 and
MC2 experienced body effect. The body effect increases Vthn, leaving a smaller
boosting voltage on CBATT than we expected. This low boosting voltage causes
higher dropout voltage when simulated with a capacitor and a charge pump.
Figs. 5.2 and 5.3 shows measured and simulated PSR values for LDO1
and LDO2, respectively. Both figures follow a similar pattern. Simulated values
are higher than measured values. At low frequencies, simulated PSR values are
84
(a) (b)
Figure 5.1: Charge Pump operation.
higher. As frequency increases the difference between simulated PSR values and
measured PSR values becomes very small. The reason behind this phenomenon
can be justified by the presence of environmental noise. At low frequencies, elec-
tronic devices introduce 60 Hz and 60 Hz harmonics. As frequency increases, PSR
values decrease, hence, measurements at higher frequencies are more tolerant to
environmental noise. Moreover, at frequencies above 1 kHz, 60 Hz harmonics are
negligible.
We were not able to compare simulated and measured AC gain and phase
because it would require opening the feedback loop in the LDOs.
5.2 Comparison with Existing Designs
The proposed LDOs are compared with both NMOS and PMOS pass tran-
sistor LDOs from the literature. Table [5.4] shows comparison of performance pa-
85
Figure 5.2: Measured and Simulated PSR values for LDO1.
rameter with other NMOS LDO. We see from table that our design has the very
low quiescent current in comparison with all other NMOS LODs. The dropout
and line regulations are among the top but total change in VOUT for load transient
is high. For LDO2, load regulation is very poor. PSR of our designs are poor in
comparison with other LDOs.
In Table [5.5] we see the comparison of performance parameter of proposed
LDOs with existing PMOS LDOs. From table we see that, we have the best
86
Figure 5.3: Measured and Simulated PSR values for LDO2.
dropout voltage and efficiency. But total change in VOUT for load transient is very
high. Quiescent current and total change in VOUT for line transient are among the
top.
5.3 Future Work
This was the first ever charge pump NMOS LDO designed in the VLSI
group at New Mexico State University. So we adopted a basic amplifier topology
87
LDO Regulator for Comparison This Work[20] [21] [2] [22] [23] LDO1 LDO2
Technology (nm) 180 350 500 350 500 180 180VDO (mV) 50 300 160 185 ≈300 177 82VDD(V ) 1.9 1.5 1.95 3.3 5 1.5 1.5VOUT (V ) 1.5 1 1.5 2.8 3.3 1.2 1.2Max Load Current (mA) 200 100 500 150 300 100 100Min Load Current (µA) 2 100 0 0 200 100 100CL (pF) 100 100 470 100 100 100IGND(µA) 70 50 517 750 6.88 6.88Line Regulation (mV/V) 10 0.1 12 1 6.7OvershootLine(mV ) 250 1000 224 90UndershootLine(mV ) 250 1100 126 72Load Regulation (mV/mA) 0.1 0.006 0.09 0.02 1OvershootLoad(mV ) 500 50 40 330 416 210UndershootLoad(mV ) 700 110 60 330 626 305Ripple(mV) 12 9 3.8PSR(dB) at fUGH 56 32 13 13Area(mm2) 0.1 0.1 1 0.1 1 0.12 0.18
Table 5.4: Comparison table with existing NMOS LDO.
to make the operation and design not too complex. There are few things that can
be done to improve this LDO performance.
The most pressing issue is the need for a better charge pump that can
boost the voltage by a desired amount.
In LDO2, the addition of a compensation capacitor to ground from the
gate of the pass transistor reduced the gain from V o2 to V i3, from near unity to
0.5. Exploring the effect on performance parameter with the change of the ratio
of this compensation capacitor and CBATT , surely deserves a chance.
Moreover, instead of a two-stage CMOS error amplifier, we can use three-
stage amplifier for higher gain, or class AB amplifier for higher slew rate for
reduced recovery time or feed-forward compensation also reduced recovery time.
88
Sta
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89
If we need higher PSR, feedforward ripple cancellation technique can be
introduced [5].
There is a good scope of optimizing the area of the chip which can be easily
reduced to around 0.05 mm2 to 0.06 mm2
And finally, adaptive biasing can be introduced, which should significantly
improve line and load transient performance of the LDOs. This technique will
increase the device area and quiescent current, however, if the LDO is used to
power highly sensitive devices, then adaptive biasing is one of the best choices.
90
APPENDICES
APPENDIX A
Test Document
A.1 With PCB:
A.1.1 Procedure to Measure Dropout Voltage VDO
1. Place the chip on the PCB. Fig. A.4 shows the dropout measurement setup.
VDD
JPVDDSUPJPVDD
JPIBIAS
IDIODE
JP1JP100MLVS
IOUTMAXJP1M
JPLOADR
VOUT
JPVREF
CLK
JPPADVDD1
JPPADVDD
Figure A.4: Jumper Configuration for Dropout measurement.
2. Apply 1.5 volt in disconnected end of the JPVDDSUP, JPIBVS and JP1.
3. Connect all the negative terminals of the power supplies to the ground pin
of the PCB.
4. Apply 1.2 volt at the jumper JPVREF.
5. Apply a 10 KHz clock at the SMA connector named CLK.
6. Place a DMM at the SMA VOUT.
7. Close the jumper JP 100 MLVS and JPVDD.
8. The resistor value of R3U was chosen using the equation (1) which is always
on.
R3U =1.2
3 · 10−6= 400kΩ (1)
93
9. Resistor value of RBIAS was chosen by equation (2)
RBIAS =1.5− 0.367
200 · 10−9= 5.67MΩ (2)
10. Value of the resistor R100ML was chosen considering 50mV drop at the end
of the current mirror using the equation (3)
R100ML =1.5− 0.7− 0.05
25 · 10−3= 30Ω (3)
11. 11. Connect 47µF capacitor with every power supply line with one end to
ground, add another 0.1µF capacitor parallel with the 47µF capacitor to
reduce the noises.
12. By hand slowly vary the voltage from 0 V to 1.5 V at JPVDDSUP. Complete
the below Table. 1 Measure the dropout voltage using the equation (4)
Vdo = Vin − Vout|Vout=Vout,max−Vout,max∗5% (4)
13. Verify that ILOAD= 100 mA for dropout measurement
A.1.2 Line Transient Test Procedure
1. The setup for line transient is shown in Fig.
2. Disconnect the capacitor from the VDD i.e the jumper JPVDD, the main
purpose to detach the capacitor is that, the capacitor does not allow the
voltage to vary 0.3 volt within 10 nano second
94
Table 1: Dropout Voltage Measurement Table
Input Voltage, Vs (V) Output Voltage, Vout (V) Load Current,IL mA0
0.20.40.60.81.01.21.251.31.351.41.451.5
3. Close the jumper JP1ML, the value of the resistor was chosen by the equa-
tion the equation (5).
R1ML =1.2
1 · 10−3= 1.2kΩ (5)
4. Now input a wave varying from 1.85 V to 1.55 V with rise and fall time
of 10 ns to SMA Connector VDD. (Note: As the function generator has
an internal resistance of 50 and the current owing through it is 1 mA, the
voltage drop across it is 50 mV. Hence, varying the input wave from 1.85V
to 1.55 V at the function generator ensures the input varies from 1.8 V to
1.5V at the VDD). The frequency of the waveform is 100 kHz
5. Procedure for Generating a 10 ns Rise and Fall Times Waveform:
Procedure for Generating a 10 ns Rise and Fall Times Waveform
95
Connect the CPU (Central Processing Unit) of the system to function gen-
erator with the help of GPIB (General Purpose Interface Bus). GPIB which
was developed by HP (Hewlett Packard), is a common protocol used by
different testing equipments for their communication. With help of probes
connect the function generator and the oscilloscope.
On the desktop, launch the waveform editor.
From the communications menu, select connection, when the connection
dialog window appears double click on GPIB::10::INSTR, then select the
Internal Type Arb and then click connect.
From the menu select Line Draw Mode, and then draw the desired waveform
with help of mouse.
After drawing the waveform, click on Send Waveform to Arb on the menu.
When the window appears, set the desired frequency and amplitude and
then click send.
Observe the waveform on the scope.
With the help of function generator, parameters like frequency, amplitude
of the waveform on the scope can be changed.
After generating Waveform, Connect the function generator to the JPVDD
6. With the help of 10x probes observe Vout waveform on oscilloscope
and measure undershoot, overshoot, line regulation, trise and tfall by using
cursor. Plot the observed waveforms.
7. Store the waveforms on digital scope and save on Portable Disk.
96
A.1.3 Load Transient Test Procedure
1. The setup for load transient is shown in Fig.
2. Disconnect the function generator from the SMA connector named VDD
3. Disconnect the jumper JP1ML
4. Disconnect the jumper JP100MLVS
5. Connect the function generator to SMA Connector IDIODE, input a wave
form that can vary from 0 to 1.5V with rise and fall time 100 nano seconds.
This way we can make the load current to vary from 3uA to 100mA
6. Connect the jumper JPVDD
7. With the help of 10x probes observe Vout waveform on oscilloscope and mea-
sure undershoot, overshoot, line regulation, trise and tfall by using cursor.
Plot the observed waveforms.
8. Store the waveforms on digital scope and save on Portable Disk.
A.2 With Bread Board
1. All the connection and procedure will be the same.
2. In the bread board there was no jumper, instead direct wire was used.
3. In the bread board connection for input was taken from four pins and two
pins for output.
4. If the solder of the IC was proper, all the eight input and output pins could
have been used.
97
APPENDIX B
Maple
99
REFERENCES
REFERENCES
[1] K. S. Thomas Szepesi, Cell phone power management re-
quires small regulators with fast response,[Available Online]:http :
//www.eetimes.com/document.asp?docid = 1225408, 2002.
[2] S.N.Easwaran, “A low power nmos ldo in the philips c050pmu process, MS
thesis, University of Twente,” March 2006.
[3] “Line and load transient testing for power supplies,” in Dallas Semiconductor,
Maxim Editorial on Power Supply Circuits.
[4] B. Razavi, Analog Integrated Circuit Design. McGraw-Hill, 2000.
[5] E. Snchez-Sinencio, “Low drop-out (ldo) linear regulators: Design considera-
tions and trends for high power-supply rejection (psr),” in IEEE Santa Clara
Valley (SCV) Solid State Circuits Society, Feb. 2010.
[6] J. Hu and M. Ismail, CMOS High Efficiency On-chip Power Management.
Springer Science and Business Medial, 2011.
[7] Power Electronics Systems Applications and Resources on Elec-
trical and Electronic Project-Thesis,[Available Online]:http :
//protorit.blogspot.com/2011/12/op− amp− distortion.html.
[8] G. A. Rincon-Mora, “Current efficient, low voltage, low dropout regulators,”
Ph.D. dissertation, Georgia Institute of Technology, November 1996.
101
[9] Phase and Gain Margins ,[Available Online]:https :
//microchip.wikidot.com/asp0107 : phase− gain−margins.
[10] M. Loikkanen and J. Kostamovaara, “Four-Stage 1.5V Class-AB Power Am-
plifier,” in Electrotechnical Conference, 2004. MELECON 2004. Proceedings
of the 12th IEEE Mediterranean, vol. 1, May 2004, p. 87.
[11] K. N. Leung and P. Mok, “Analysis of multi-stage amplifier-frequency com-
pensation,” IEEE Transactions on Circuits and Systems I: Fundamental The-
ory and Applications, vol. 48, no. 9, pp. 1041–1056, Sep. 2001.
[12] P. Furth, “Lecture note 1 of Integrated Power Management, New Mexico
State University,” January 2013.
[13] G. Palumbo and S. Pennisi, “Design Guidelines for Optimized Nested Miller
Compensation,” in Southwest Symposium on Mixed-Signal Design, 2000.
SSMSD. 2000, Feb. 2000, p. 97.
[14] Y.-H. Cheng, “A Novel Feedforward Reversed Nested Miller Compensation
Technique for Three-Stage Amplifiers,” in 8th International Conference on
Solid-State and Integrated Circuit Technology, 2006. ICSICT ’06, Oct. 2006,
p. 1788.
[15] F. Zhu, S. Yan, J. Hu, and E. Sanchez-Sinencio, “Feedforward Reversed
Nested Miller Compensation Techniques for Three-Stage Amplifiers,” in
IEEE International Symposium on Circuits and Systems, 2005. ISCAS 2005,
May 2005, p. 2575.
[16] V. Saxena and R. Jacob Baker, “Compensation of cmos op-amps using split-
length transistors,” pp. 109–112, Aug 2008.
102
[17] R. J. Baker, CMOS Circuit Design, Layout, and Simulation, 3rd Edition.
Wiley-IEEE Press, 2000.
[18] D. P. G. James C. Daly, Analog BiCMOS Design: Practices and Pitfalls, 1st
Edition. CRC Press, 1999.
[19] Lecture note on Electronic Circuits ,Zagazig University, [Available
Online]:http : //www.staff.zu.edu.eg/mfarahat/userdownloads/Courses/ECE321.
[20] S. Chakingal and P. Chandramohan, “Design of ultra low drop-out regulator
for audio devices,” MSRUAS-SASTech Journal, vol. 13, no. 2, 2012.
[21] G. Giustolisi, C. Falconi., A. DAmico, and G. Palumbo, “On-chip low drop-
out voltage regulator with nmos power transistor and dynamic biasing tech-
nique,” Analog Integr Circ Sig Process, vol. 58, no. 9, pp. 81–90, 2009.
[22] M. C. Choi, “Low-dropout linear regulators with q reduction, MS thesis,
Tatung University,” July 2011.
[23] G. W. den Besten and B. Nauta, “Embedded 5 v-to-3.3 v voltage regulator
for supplying digital ics in 3.3 v cmos technology,” IEEE JOURNAL OF
SOLID-STATE CIRCUITS, vol. 33, no. 7, 1998.
[24] B. P. F. Hazucha, Karnik and S. Borkar, “Area-efficient linear regulator with
ultra-fast load regulation,” Solid-State Circuits, IEEE Journal, vol. 40, no. 4,
pp. 933–940, 2005.
[25] R. Milliken, Silva-Martinez and E. Sanchez-Sinencio, “Full on-chip cmos low-
dropout voltage regulator,” Circuits and Systems I: Regular Papers,IEEE
Transactions on, vol. 54, no. 9, pp. 1879–1890, 2007.
103
[26] T. Man, P. K. T. Mok, and M. Chan, “A high slew-rate push-pull output
amplifier for low-quiescent current low-dropout regulators with transient-
response improvement,” Circuits and Systems II: Express Briefs, IEEE
Transactions on, vol. 54, no. 9, pp. 755–759, 2007.
[27] E. Ho and P. K. T. Mok, “A capacitor-less cmos active feedback low-dropout
regulator with slew-rate enhancement for portable on-chip application,” Cir-
cuits and Systems II: Express Briefs, IEEE Transactions on, vol. 57, no. 2,
pp. 80–84, 2010.
[28] P. Y. Or and K. N. Leung, “An output-capacitorless low-dropout regulator
with direct voltage-spike detection,” Solid-State Circuits, IEEE Journal of,
vol. 45, no. 2, pp. 458–466, 2010.
[29] J. Guo and K. N. Leung, “A 6- µw chip-area-efficient output-capacitorless ldo
in 90-nm cmos technology,” Solid-State Circuits, IEEE Journal of, vol. 45,
no. 9, pp. 1896–1905, 2010.
[30] M. Ho and K. N. Leung, “Dynamic bias-current boosting technique for
ultralow-power low-dropout regulator in biomedical applications,” Circuits
and Systems II: Express Briefs, IEEE Transactions on, vol. 58, no. 3, pp.
174–178, 2011.
[31] X. Ming, Q. Li, Z. kun Zhou, and B. Zhang, “An ultrafast adaptively biased
capacitorless ldo with dynamic charging control,” Circuits and Systems II:
Express Briefs, IEEE Transactions on, vol. 59, no. 1, pp. 40–44, 2012.
[32] S. Chong and P. Chan, “A 0.9- µa quiescent current output-capacitorless
ldo regulator with adaptive power transistors in 65-nm cmos,” Circuits and
104
Systems I: Regular Papers, IEEE Transactions on, vol. 60, no. 4, pp. 1072–
1081, 2013.
[33] E. Ho and P. K. T. Mok, “Wide-loading-range fully integrated ldr with a
power-supply ripple injection filter,” Circuits and Systems II: Express Briefs,
IEEE Transactions on, vol. 59, no. 6, pp. 356–360, 2012.
105